NASA SP-290
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TIIItI|INI{
I)KSll;l
a,id AI'I'I, II:AI'IIiN
(NASA-SP-290) APPLICATION
TURBINE (NASA)
DESIGN 390
N95-22341
AND
p Unclas
HlI07
NATIONAL
AERONAUTICS
AND
SPACE
0041715
ADMINISTRATION
NASA
SP-290
'lrlllel|lNl IDK Iq ,N annalAIDIDI,Iq;A"I' IqlPm
Edited by Arthur J. Glassman Lewis Research Center
Scientific and Technical Information Program--1994 NATIONAL AERONAUTICS AND SPACE ADMINISTRATION Washington,
DC
Available NASA
from the Center
800 Elkridge
for AeroSpace Landing
Linthicum Heights, Price Code: A17 Library
of Congress
Information
Road MD 21090-2934 Catalog
Card Number:
94-67487
PREFACE NASA and
has
space
an interest
turboshaft
spacecraft.
fluids,
interest
for turbine
trains,
etc.)
In view a
Program.
The
1972-73.
Various
entitled
course and
velocity
cooling, The
mechanical notes written
edited
for
are the
U.S.
sets
of units
units
and
after
Such
set
of
will
satisfy
units
consistent symbol
customary
units.
by including defining
a
Research
Application"
was
Graduate again
were
Study
presented
covered
can
serve
means
for
in
including
fundamental
aerodynamic
course,
power.
at Lewis
and
a publication
buses,
turbine design,
blade
revised
and
as a foundation self-study,
or
topics.
used the
and
blade
of
trucks,
In-House
concepts,
losses,
turbine
consistent
Design revised
providing
electrical
efforts
technology
gases,
applications
(cars,
and the
auxiliary
for
Other
and l%o-
inert
design, operation, and performance. and used for the course have been
for selected
given
somewhat of turbine
diagrams,
publication.
commonly
of
fluid-dynamic
introductory
Any
part
using
ground-based
interest as
was
aspects
concepts,
Two
and
aircraft,
studied
land-vehicle
"Turbine
1968-69
thermodynamic
an
power
been
jet
and
engines
spacecraft.
include
for
propulsion
have
for
to aeronautics provide
power
turbine
fluids
power
turbine-system
during
reference
rocket
engines
course
presented
engines
provide
propulsion
of the
primarily
turbine
as auxiliary
metal
electric
related
well
Closed-cycle
and
long-duration
Center,
as
turbines
for
organic
for
Airbreathing
propulsion,
pellant-driven power
in turbines
applications.
as unity
sets
of
definitions. A
single
all constants those
not
,°°
111
the units
These set
of
required required
equations and are
presented.
constant the
SI
equations for the
values units
covers U.S.
and both
customary
for the SI units. ARTHUR J. GLASSMAN
a
i _
,_
CONTENTS CHAPTER
PAGE
PREFACE
°
• • • • • • • • • • • • • • • • • • • • • • • • • • • • • • . . . . . . . . . . .
THERMODYNAMIC CONCEPTS
AND
by Arthur
FL UID-D
YNAMI
J. Glassman
C
....................
BASIC CONCEPTS AND RELATIONS ....................... APPLICATION TO FLOW WITH VARYING AREA REFERENCES ...................................... SYMBOLS .........................................
,
BASIC
TURBINE
CONCEPTS
by Arthur
1 1 14 19 20
..............
J. Glassman
....
TURBINE FLOW AND ENERGY TRANSFER .................. DIMENSIONLESS PARAMETERS ......................... REFERENCES ...................................... SYMBOLS ......................................... GLOSSARY .........................................
.
VELOCITY DIAGRAMS by Warren Warner L. Stewart ...................................
J. Whitney
BLADE Arthur
DESIGN
by Warner
J. Glassman
21 45 62 63 65
and
L. Stewart
STUDIES
.....
CHANNEL
FLOW
ANALYSIS
lOl
.
INTRODUCTION by William
102 118 124 125
by Theodore
STREAMAND POTENTIAL-FUNCTION VELOCITY-GRADIENT ANALYSIS REFERENCES ...................................... SYMBOLS .........................................
ANALYSES ........................
TO BOUNDARY-LAYER
D. McNally
70 84 95 96 98
and
..................................
SOLIDITY .......................................... BLADE-PROFILE DESIGN .............................. REFERENCES ...................................... SYMBOLS .........................................
,
21
69
MEAN-SECTION DIAGRAMS ............................ RADIAL VARIATION OF DIAGRAMS ....................... COMPUTER PROGRAMS FOR VELOCITY-DIAGRAM REFERENCES ...................................... SYMBOLS .........................................
,
...
111
Katsanis ............
......
127 130 147 154 155
THEORY
...............................
157
NATURE OF BOUNDARY LAYER ......................... DERIVATION OF BOUNDARY-LAYER EQUATIONS SOLUTION OF BOUNDARY-LAYER EQUATIONS CONCLUDING REMARKS .............................. REFERENCES ...................................... SYMBOLS .........................................
............ ..............
157 160 172 188 188 191
V
iI
PAG'E__
I_T_NTtON_!.Ly BLANg
CHAPTER
o
PAGE
BOUNDARY-LAYER
LOSSES
by Herman
W. Prust,
Jr ....
BOUNDARY-LAYER PARAMETERS ........................ BLADE-ROW LOSS COEFFICIENTS ....................... BLADE-ROW LOSS CHARACTERISTICS .................... REFERENCES ....................................... SYMBOLS .........................................
o
MISCELLANEOUS
LOSSES
by Richard
195 201 217 221 223
J. Roelke
........
225
TIP-CLEARANCE LOSS ................................ DISK-FRICTION LOSS ................................. PARTIAL-ADMISSION LOSSES ........................... INCIDENCE LOSS .................................... REFERENCES ....................................... SYMBOLS ..........................................
o
SUPERSONIC
TURBINES
by Louis
225 231 238 243 246 247
J. Goldman
.........
METHOD OF CHARACTERISTICS ......................... DESIGN OF SUPERSONIC STATOR BLADES ................. DESIGN OF SUPERSONIC ROTOR BLADES .................. OPERATING CHARACTERISTICS OF SUPERSONIC TURBINES REFERENCES ....................................... SYMBOLS .........................................
10.
RADIAL-INFLOW
TURBINES
by Harold
E. Rohlik
OVERALL DESIGN CHARACTERISTICS .................... BLADE DESIGN ..................................... OFF-DESIGN PERFORMANCE ........................... REFERENCES ....................................... SYMBOLS .........................................
11.
TURBINE
COOLING
by Raymond
S. Colladay
EXPERIMENTAL DYNAMIC and Harold
DETERMINATION PERFORMANCE by Edward J. Schum ................................
....
.......
250 263 266 272 277 278
279
...........
307 307 314 328 330 332 340 345 347
OF AEROM. Szanca
TEST FACILITY AND MEASUREMENTS .................... TURBINE PERFORMANCE .............................. REFERENCES ....................................... SYMBOLS .........................................
vi
249
284 295 302 305 306
GENERAL DESCRIPTION .............................. HEAT TRANSFER FROM HOT GAS TO BLADE ................ CONDUCTION WITHIN THE BLADE WALL .................. COOLANT-SIDE CONVECTION ........................... FILM AND TRANSPIRATION COOLING ..................... SIMILARITY ........................................ REFERENCES ....................................... SYMBOLS .........................................
12.
193
351 352 374 387 388
CHAPTER 1
Thermodynamic andFluid-Dynamic Concepts ByArthur J. Glassman This
chapter
cepts are
of the
is intended
thermodynamics concepts
energy-transfer treatment textbooks. the
U.S.
needed
to
processes
purposes
given
and
of this
consistent commonly after
units
by
units
and
of
analyze
including
units
will
all
sets
must
know
generalizations of behavior,
The
flow
more
concerning are
far
how
not
and
complete
of
with
their
covers the
for
U.S.
the
values
are
and
the
units both
sets
of
customary
SI units.
RELATIONS
kind
of calculation
volume,
and
resulted
in
behavior. to
SI
State
any has
presented.
constant the
for
required
AND
gases
referred
and
of equations
pressure,
of
equations
are
required
those
very
study
gases
of units
set
CONCEPTS
get
we
These
the A
the
These
constants
as unity
we can
interrelated.
turbine.
satisfy
Equation
gases,
mechanics.
understand
a
con-
can be found in reference 1 and in many to be steady and one-dimensional for
A single
BASIC
Before
fundamental
fluid
and in
definitions.
units.
defining
compressible
consistent
symbol
customary
of the
chapter. set
used
the
some
occurring
of these subjects Flow is assumed
Any Two
to review
as being
In
temperature certain
discussing
either
involving
ideal
laws these or real.
are and laws The
TURBINE
DESIGN
ideal
is only
the
gas real
The
gas
AND
hypothetical
can
ideal
APPLICATION
only
gas
and
approach
equation
obeys
under
of state
various certain
simplified
laws
that
conditions.
is R*
T
pv=--_-
(1-1)
where P
absolute
pressure,
V
specific
R*
universal gas constant, (lb mole) (°R)
volume,
molecular
lb/ft 2
m3/kg;
weight,
absolute The
N/mS;
fta/lb 8314
kg/(kg
temperature,
quantity
R*/M,_
J/(kg
mole); K;
is often
1545
mole)(K);
lb/(Ib
(ft) (lb)/
mole)
°R used
as
a single
quafftity
such
that
R $
R-----_-_ where
R is the
Density law.
gas
constant,
is often
used
(1-2)
in J/(kg)(K)
instead
or
of specific
(ft)(Ib)/(lb)(°R). volume
in
the
ideal
gas
Thus, 1 p =-
where
p is density,
In
general,
sures
or
within
high
as 50 atmospheres, deviations
of several None
applicable
only
pressure. to use
similarity (ratio
pressure
2
between
above their critical to within 5 percent for
and
gases
may
below
appear
ideal
been the
cannot
their
free
over
have
the as
pressure.
to express
in the the
p-v-T
satisfactory, range
of these
justified
are
tempera-
resulted
a limited
useful
space
molecules
critical
universally
gas
pres-
temperatures, up to pressures
of state
most be
the
low
at 1 atmosphere
behavicr
found
to a single Even
in behavior
and
reduced
behavior.
which
forces
at
unless
and of tem-
equations
a high
are
degree
of
is required.
temperature forms
under
equations
have
behavior
attractive
from
hundred
of these
and
cumbersome The
gases
ideal
conditions the
while
of real
relation.
accuracy
and
which are be accurate
proposal are
(1-3)
approximate
of 2 to 3 percent
Deviations
perature
will
temperatures,
For gases gas law may
most
gas
gas is large
small. ideal tures,
RT = pRT
in kg/m 3 or lb/ft 3.
a real
high
the
V
the
of
of substances
temperature, (ratio
basis
of a relatively
The
method
of
T,
of pressure, simple general
at equal to
critical
p,
method correlation
values
of reduced
temperature,
to critical for
estimating is
to
To)
pressure, real
incorporate
pc) gas a
THERMODYNAMIC
correction law:
term,
called
the
AND
FLUID-DYNAMIC
compressibility
factor,
CONCEPTS
into
the
ideal
gas
p=zpRT where
z is the
The and
compressibility
compressibility
reduced
of the
gas.
Values
temperature other as
figure
with
for
This
may
and
pressures
be
are
The
molal
averages
of
calculations
do
never
quick
not
determination
approximate
error
of
the
associated
we
the
are
use
of the
pres-
using
the
law
ideal
in our
However, is always
factor
can
gas
of
in a large with
region. gas
region
result
concerned
this ideal
by
would
compressibility with
and
is a large
law
within
that
temperatures
components.
there
gas
that
fall
granted
average correla-
approximated
that
ideal
and here
agreement
temperatures
of the
shows
usually
for
an
if pseudocritical are
conditions
from
in rigorous
reduced
properties
of the
texts
compressibility-factor
mixtures
1-1
use
of reduced
in many
is not
The
nature
2 is reproduced
is derived
properties
figure
temperature of the
as a function
presented
and
to calculate
the
take
gas.
critical
where
Fortunately,
should
one
reduced
reference
correlation
to gas
used
are from
of gases
any
of the
conditions
error.
of
pseudocritical
Examination
A
for
extended
sures.
state
type
of
to be independent factor
charts
number
data
tion
a function
pressure
of the
a large
all the
is
is assumed
reduced
One
1-1.
of data
and
of compressibility
and
sources.
factor.
factor
pressure,
(1-4)
we valid.
show
the
I 9,0
F 10.0
law.
Reduced temperature, 1.20 T/Tc_ 1.10 1.00
_
_--
_._
--
1. 1_50
______
N
•90 .80 • 70 t_
.60
--
1.20
.50
-
I \ -1.1o
.30! _-'LO0 1.0
I 2,0
I 3,0
1 4.0
I 5.0
f 6.0
I 7.0
I 8.0
Reduced pressure, P/Pc
FIGURE
1-1.--Effect
of
reduced
pressibility
pressure factor.
(Curves
and
reduced from
ref.
temperature
on
com-
2.)
3
TURBINE
DESIGN
AND
Relation In
a flow
is the and
of
process,
enthalpy
position,
APPLICATION
Energy the
h. For
enthalpy
Change
energy
term
a one-phase
can
be
to
State
Conditions
associated
system
expressed
as
with
work
of constant a
and
chemical
function
of
heat com-
temperature
pressure: h=fcn(T,
where
h is specific
enthalpy
can
enthalpy,
in J/kg
be expressed
partial
derivatives
properties
as follows.
can By
(1-5)
or Btu/lb.
A differential
change
v dT+(00-_h)rp be
expressed
dp in
(1-6) terms
of
determinable
definition, Oh Cv=(-_'_),
where
cp is heat
(lb) (°R).
One
capacity
of the
at
basic
constant
differential
dh=
where s is specific entropy, conversion constant, 1 or derivative
with
determined
respect
from
of the
Maxwell
pressure,
in J/(kg)(K)
equations
of thermodynamics
pressure
or Btu/
vdp
at
is
(1-8)
in J/(kg)(K) or Btu/(lb)(°R), 778 (ft)(lb)/Btu. Therefore,
to
equation
(1-7)
Tds + j
constant
and J is a the partial
temprature
is,
as
(1-8), Oh'_
One
in
as
Oh dh:(-O-T) The
p)
relations
T los\
states
1
that
(1-10)
Substituting
equations
(1-7),
(1-9),
and
(1-10)
j
Ov T (_-_)p_
into
equation
(1-6)
yields dh=c,dT+
Equation change between 4
(1-11)
in
terms
two
states
is the of
the
rigorous state
is calculated
[v--
equation conditions, rigorously
for and as
dp
(1-11)
a differential the
enthalpy
enthalpy change
THERMODYNAMIC
Ts
AND
1
FLUID-DYNAMIC
P*
CONCEPTS
_V (1-12)
If
we
law,
now
assume
we can
that
the
gas
behaves
according
to
the
ideal
gas
set RT v------P
(1-13)
and
( Ov' By
using
these
pressure
on
last
two
enthalpy
equations
change
Empirical
equations
and
in
for most
gases
of equation
Although
one
might
calculations, If and
there
it can
be
/'2, then
not
bT+cT
assumption
gases,
there
of some
average
be within
usually loss,
value
a few
Relation In
is an
there
cv will
of the
true
Conditions
the
loss
be is no
heat
assumed change
in hand-
example,
(1-17)
type it for
of expression computer
between
for hand calculations.
temperatures
T_
T2-- T1) one
of State
a turbine, can
percent
available
If, for
(_--T_)
this
for
variation
for
remains
(1-16)
ca is constant
excellent
is a significant
of
becomes _=c.(
This
there
2
to avoid
that (1-15)
effect
yields
to use
reason
assumed
equation
and
of T are
of interest.
(1-15)
want
is no
the
(1-15)
T2-- T1) +_ b (_--_)+3
Ah=a(
(1-12),
to zero,
for ca as a function
textbooks
integration
equation
frTcz, dT
cp=a-tthen
(1-14)
is reduced
Ah:
books
R
to be
monatomic
in c_ with give
an
gases;
for
T. However,
approximation
other
the
that
use
should
value. for
Constant
is normally adiabatic.
in entropy.
(1-18)
small, For
Therefore,
Entropy
Process
and
flow
the
adiabatic the
flow
process with
no
constant-entropy
(isentropic) process is the ideal process for flow in the various parts of the turbine (inlet manifold, stator, rotor, and exit diffuser) as well as for the overall turbine. Actual conditions within and across the
TURBINE
DESIGN
AND
APPLICATION
turbine are usually determined in coniunction necessary For can
with
to be able a one-phase
some
state
conditions
of constant
as a function
a differential
From
change
equations
Substituting
(1-8)
(1-23)
we get
(1-21)
and
relating
temperature
If we assume into
equation
and
pressure
ideal-gas-law (1-23)
and
but
using
a relation
such
equation
(1-17),
a computer calculation With the additional
not
behavior the
as equation
peratures 6
T_ and
equation
equation
(1-25)
(1-24)
yields
(1-22)
particularly
and
useful,
expression
for an isentropie substitute
integration,
process.
equation
(1-14)
we get
Rln_
(1-24)
(1-16),
integration
yields
(T_--T_)
also
is more
becomes
(1-25)
suitable
than in a hand calculation. assumption that cp is constant
T2, equation
(1-20)
dp
1Rln_=aln_--kb(T2--T_)+2 J p_ Like
(1-20)
and
, _dT----
By
into
conditions
perform
as
(tp
0v (0-T),
ds=0
rigorous,
entropy
pressure (1-19)
(1-10)
dT--j
process,
is the
composition, and
be expressed
and
a constant-entropy
Equation
can
dT÷(_)r
equations
process.
(T, p)
ds----(_),
ds=_
For
chemical
in entropy
(1-7),
It is, therefore,
for an isentropic
of temperature s----fcn
and
isentropic process calculations
efficiency or loss term.
to relate system
be expressed
from
for use
between
in
tem-
THERMODYNAMIC
AND
Jc_ ln T2--R T1--
FLUID-DYNAMIC
CONCEPTS
p2 ln- pl
(1-26)
and p2=('%'_ p, \T1/
Jc,/R (1-27)
But Jcp R where
3" is the
capacity equation
ratio
of heat
at constant (1-27) yields
3' 3"-- 1
capacity
(1-28) at
constant
volume. Substitution of the more familiar form
pressure
equation
to
heat
(1-28)
into
p, _-_----\_]
Where should
specific heat ratio give a reasonable
(1-29)
3" is not constant, approxlmation. Conservation
The
rate
of mass
flow
through
the
use
of an average
value
of Mass an area
A can
be expressed
as
w=pAV
(1-30)
where w A
rate flow
of mass flow, kg/sec; area, m2; ft 2
V
fluid
velocity,
For across across
a steady any any
m/see; flow
lb/sec
ft/see
(and
nonnuclear)
section of the flow other section. That
path is,
process, must
equal
the
rate
of mass
flow
the
rate
of mass
flow
plA, VI = p2A2 V2 This
expresses
(1-31)
the
is referred
principle to as the
of conservation continuity
Newton's
are
All conservation
equations,
consequences
of Newton's
that an unbalanced in the direction force is proportional the body.
Second
Law
Second
product
of mass,
and
equation
equation.
theorems,
force that ac_s of the unbalanced to the
(1-31)
of etc.,
Law
Motion dealing of
with
Motion,
momentum which
states
on a body will cause it to accelerate force in such a manner that the of the
mass
and
acceleration
of
7
TURBINE
DESIGN
AND
APPLICATION
Thus, F= m a g
(1-32)
where F
unbalanced
force,
m
mass,
a
acceleration,
g
conversion
kg;
N;
lbf
lbm m/sec2
; ft/sec
constant,
2
1 ; 32.17
(lbm)
(ft)/(lbf)
(sec 2)
But dV a =--d- 7 where
t is time,
(1-32)
in seconds.
Substituting
the
mass
is constant,
into
equation
g Equation
(1-34b)
is equal mass
(1-34a)
can
to
specifies the
(1-34a)
equation
F=I
Since
(1-33)
dV dt
g
fluid
equation
yields F=m
Since
(1-33)
rate
(1-34a)
the
of
also
be written
as
be
written
time
F =w
as
(1-34b)
unbalanced
of change
increment
also
d(mV__) dt
that
per
can
force
of momentum is the
mass
acting
(mV) flow
on
with
rate,
the
time.
equation
dV
(1-35)
g
be
A useful derived
fluid
as indicated
ligible. of
relation, sometimes called the from second-law considerations.
A fIictional
fluid
forces
in figure resistance
is subjected acting
in
Expanding,
Gravitational (force)
downstream in
+(p+
simplifying,
and direction
the upstream direction is
of are
assumed
can of neg-
element
boundary-surface-pressure and
fluid-pressure Therefore,
(A+dA)--dRt
second-order
dropping
motion, an element
as R s. The
direction.
d-_)dA--(p+dp)
and
forces
is indicated
to fluid-pressure the
friction forces acting force in the downstream
F=pA
1-2.
equation Consider
and the
net
(1-36)
differentials
yields F= 8
-- Adp--
dR I
(1-37)
THERMODYNAMIC
The
mass
of the
element
AND
FLUID-DYNAMIC
is m:pAdx
Substituting
CONCEPTS
equation
(1-38)
into F_
(1-38)
equation
pAdx g
(1-34)
yields
dV dt
(1-39)
Since
(1-40) equation
(1-39)
can
be written
in the
form
F_pAV
dv
(1--41)
g Equating
(1-37)
with
(1-41)
now
yields
F=--Adp--dRs=
pA VdV g
(1-42)
and dp + VdV+
dRs
0
p-F--i-A--
(1-43)
p+dp 2
A+dA f f
% ,%
Flow
p+dp
p dx
V+dV
V
dRf FIGURE
1-2.--Forces
on
an
element
of
fluid.
TURBINE
DESIGN
If we now
AND
APPLICATION
let (1-44)
where
ql is heat
produced
by
friction,
in J/kg
dpp __V_VdgV+Jdq1= For
isentropic
flow,
a steady-flow
a system system
or or
electrical
(and
part
of of that
energy,
etc.,
(1-45)
0
P lvl
equal
If
we still
"Jr- V12
Energy process,
must
system.
kinetic energy work I¥,. Thus,
u,+--j-
of
nannuclear)
a system
part
energy pv, mechanical
we have
dqs----0. Conservation
For
or Btu/lb,
we
have
energy Z,
heat
J-J--
that energy, u, flow q,
and
(1-46)
V2" 2 .4 Z_2_4_W Tr
j-2g
entering
leaving
chemical
internal energy
p2l'2_l__ ,
-j+q=u:+
energy
energy
neglect
potential
_j[_Z1
_gj
the
can
to consider
V2/2g,
the
s
where u
specific
internal
Z
specific
potential
q W,
heat added mechanical For
by
energy,
J/kg;
energy,
to system, work (lone
a gas system,
the
Btu/lb
J/kg;
(ft)
(lbf)/lbm
J/kg; Btu/lb by system, J/kg;
potential
energy
can
Btu/lb be neglected.
In addition,
definition pv
(1-47)
h=u + -j Thus,
equation
(1-46)
reduces
to V
"{72
2
(1-48) gd Equation
(1-48)
as we will be using
is the
basic
g form
The
sum
of the
problems,
steady-flow
energy
balance
it. Total
in flow
of the
enthalpy and
and
Conditions the
kinetic
it is convenient
energy
to use
is always
it as a single
appearing quantity.
Thus, V2 h ' _-h + 2gJ 10
(1-49)
THERMODYNAMIC
where
h' is total
The
enthalpy,
concept
of
temperature. that
corresponds
cept
is most
capacity
to
the
leads can
total
when
us
be
enthalpy.
In
that
to
the
defined The
ideal-gas-law
be assumed.
FLUID-DYNAMIC
CONCEPTS
or Btu/lb.
enthalpy
temperature
useful
can
in J/kg
total
Total
AND
as
the
of
temperature
and
according
con-
constant
heat
to equation
(1-15),
h'--h=cp(T'--T) where
T'
with
is total
equation
temperature,
(1-49)
(1-50)
in K or °R.
Combining
equation
(1-50)
yields V2
T' = T+ 2gJcp The
total
attained
temperature
when
to rest The
total,
pressure
T'
can
at static
these
total
two
brought
equation
of
T and
can
between
as
the
temperature
velocity
is also
used
V is brought
called
stagnation
interchangeably. be regarded
isentropically
relation
(1-29)
are
pressure
to rest the
thought
temperature
terms
or stagnation,
p. Since
be
(1-51)
temperature
Thus,
and
of a fluid use
a gas
adiabatically.
temperature,
total
total-temperature
behavior
case,
concept
from p'
as the
a velocity
and
pressure
V and
p is isentropic,
static we can
to write
(1-52)
where
p'
With
is total
pressure,
regard
to the
in N/m 2 or lb/ft _. above-defined
total
conditions,
certain
points
should its use
be emphasized. The concept of total enthalpy is general, involves no assumptions other than those associated with
energy
balance
be seen,
as we have
is a very
tion,
but
heat
capacity.
useful
it is rigorous For
change,
the
use
pressure,
in addition
ture, involves conditions. Flow Let occurs work. each
us now, with This part
in
neither process
of the
only
for
systems
of an
considered
it.
convenience
total
temperature
to the
assumptions
is
With
terms
of total
conditions,
transfer
(adiabatic
heat
turbine
one
No
that
(including
not
between
Heat
occurs the
rotor,
and
of calculaand
reaction
constant
or
a
recommended.
associated
path
as will
burden
behavior
chemical
Process
is the
temperature, the
ideal-gas-law
involving
isentropic
Total
for easing
with
static
No
Work
examine process) (neglecting at constant
phase Total
total
the
and the
temperaand
total
a process
that
nor
mechanical
heat
losses)
radius,
in
when 11
TURBINE
the
DESIGN
velocities
AND
are
expressed
Substitution
of
rangement
APPLICATION
relative
equation
to the
moving
into
equation
(1-49)
blade). and
(1-48)
rear-
yields h2' -- hi' = q--W_
The
energy
dynamics
balance for
If we set
now
a flow
q and
looks
something
process,
W_
equal
as we
to zero,
(1-53)
like
were
the
first
First
Law
exposed
of Thermo-
to it in college.
we get
h_' =-h,' Therefore,
for
constant. that
adiabatic
Further,
total
flow
from
with
no
equations
temperature
also
(1-54) work,
(1-18)
remains
total
and
enthalpy
(1-50),
remains
it can
be shown
constant.
TJ =T/ Note
that
the
enthalpy Total and
process
and
total
pressure
(1-55)
tions,
not
have
the
matter.
ideal-gas-law
be shown
to be isentropic
to remain
is another
and
it can
does temperature
that
(1-55)
From
and
for
in order
for total
(1-22),
(1-52),
constant. equations
constant-heat-capacity
adiabatic
flow
with
assump-
no work,
eJd' l _= P_' p2' Only
for isentropic
constant.
For
flow
flow
(ds=0),
with
(1-56)
therefore,
loss
(ds>0),
does there
total is
pressure
remain
a decrease
in
total
pressure. Speed An wave
important
of
Sound
and
characteristic
propagation
or,
as
of
otherwise
small-pressure-disturbance
Velocity gases
is
called,
the
Ratios the
speed
speed
of
of sound.
From
a is speed the
ideal
of sound, gas
From
theory
a=_/g(-_p), where
pressure-
law
in m/sec and
(1-57) or ft/sec.
isentropic
process
relations,
this
reduces
to a= The factor called 12
ratio
of fluid
velocity
in determining the flow the Mach number M:
V
_gRT to sound characteristics
(1-58) velocit_y
a is an important
of a gas.
This
ratio
is
THERMODYNAMIC
AND
FLUID-DYNAMIC
CONCEPT_
M= --V
(1-59)
a
Mach
number
is a useful
behavior regimes, but expressions. Consider temperature, (1-59),
given
and
parameter
also the
with
(1-51).
equation
ratio
for
Combining
(1-51)
T'
Another velocity critical velocity
only
identifying
for simplifying and generalizing relation of total temperature
in equation
(1-28)
not
to
equations
certain static (1-58),
yields
l_I_7__
often
flow-
(1-60)
M 2
used
is the
ratio
of fluid
velocity
V V Vc,--acr where
V.
sound
at
is critical critical
is equal
to the
condition (1-60),
at
velocity,
velocity
(1-61)
in m/sec
condition,
in m/sec
of sound
or or
at the
is that condition where the critical condition
to
ft/sec, ft/sec.
critical
M----1.
and The
a.
is speed
critical
condition.
The
Consequently,
of
velocity critical
from
equation
2 T.=3"+ and
substitution
of equation
1 T'
(1-62)
into
(1-62) equation
(1-58)
yields
(1-63)
acr=_/_lgRT' Thus,
in any
no work),
flow process
the
value
of the
for the
entire
process,
as
the
static
temperature
The
ratio
the
critical
because while perature The
the Mach
constant
critical
whilethe
of fluid velocity
with
velocity value
velocity ratio.
to
Its
(Vc,=a,)
of the
critical
speed
velocity
use is often
velocity
ratio
number
is not
(since
the
temperature
(no heat remains
of sound
and
constant (a) changes
changes.
critical
in
total
preferred
is directly there
is sometimes over
proportional
is a square
root
Mach
called number
to velocity, of static
tem-
denominator).
relation
between
critical
velocity
ratio
(1-28),
and
static results
and from
total
temperature
combining
equations
in terms (1-61),
of the (1-63),
(1-51). TT '-1
3,--1(V) 3"-t-1 _
2
(1-64) 13
TURBINE
DESIGN
AND
APPLICATION
APPLICATION The the
equations
flow
(flow the
TO
already
through
in the turbine.
there
to learn
varying-area
passages
We
are
going
change,
ously
to
and
presented
examine
number.
equations
yields
to analyze
are
losses
in a turbine,
we can
about
the
of the
rotor,
are
behavior
and
exit
no
losses
diffuser)
use flow
of the
Regime
relations
a,mon_
Prot)er the
there
completely
that
Flow
the
Much
AREA
provided
(stator, of
VARYING
sufficient
something
Effect
area
are
passages,
Although
process
WITH
presented
turbine
is isentropic). loss-free
FLOW
pressure,
manipulation
following
velocity,
of the
equation
previ-
for isentropic
flo_v:
_(I_M_
Equation
(1-65)
velocity
is opposite
the
changes
whether let
flow),
static
to the
Much
Let
Much
with than
the
various
flow
(M
1. Increasing
flow).
cases
pressure
Decreasing
flow
Increasing Velocity This
This
way
passage
from
equal
to
1
of definition,
in which passage
static
in
equation
which
flow
(M=
Area
change
mum-area
increases
(dA>0).
and
area
decreases
(dA_0).
and
area
(tecreases
area
increases
(dA_0).
diffuser. (dV>0)
supersonic
increasing
:
(dp<0):
increases
Both
(1-65)
area
(dp>0): (dV<0)
pressure
is the
critical,
14
on
(M>I):
supersonic
Decreasing
Sonic
of
depend
(dp<0):
pressure decreases
is the
Velocity C.
directions
flow),
By
in
(dp>0):
pressure
Supersonic
2.
change
in area
is a varying-area
Velocity increases (dV>0) This is the subsonic nozzle.
1.
(2) the
1 (subsonic
Velocity decreases (dV<0) and This is the subsonic diffuser..
B.
amt
the
increases.
Subsonic
2.
numbers
is a varying-area
a diffuser
(1-65)
changes
1 (supersonic
us examine A.
all
dA A
in l)ressure
is less
than
and
for
pressure
a nozzle
decreases
1--M 2alp 7M 2 p
change
number
that
pressure
(1)
and
or greater
us specify
pressure
that
in velocity
the
(sonic
shows
)dV V--
and
(dA>0).
nozzle.
1) : (dp>0) must
condition section
and
equal can
zero
occur
decreasing
(dp<0)
(dA=0). only
of a varying-area
at
the
pressure.
Thus,
the
inlet,
exit,
passage.
sonic,
or
or mini-
THERMODYNAMIC
You
may
dition
also
(M=
must
want
to note
1) going
have
either
AND
that
up
in order
or down
a decreasing-area
FLUID-DYNAMIC
portion
CONCEPTS
to cross
the
in velocity, followed
critical
the
by
an
flow
con-
passage
increasing-area
portion. Flow Since
we
diffuser nozzles.
are
the
nozzle
Convergent nozzle.
primarily
nozzle
the
gas
is subsonic,
nozzle.--Let
This
the
at
T'.
as p, and is designated
mences
and
the
lowered,
flow
At
value
some
velocity,
and
of p,, M=
Mach
number
nozzle.
Therefore,
tion
(M=
the
throat
remains and
lowered
than
the
flow
at
the is
pe is reduced flow
much
the
nozzle
and
then
expansion
with the
the
an
isentropic The fact
pressure ratio
(p'/p_r)
constant the mass
be
throat
the
exhaust
and
the
pressure
to maximum
com-
equal
to pc. to sonic
from
will
than
the
The
a
that condi-
pressure
according
from
mass
to equa-
no
with
shocks
pr6ver_
to the
fact
nozzle.
(which
occur
no
matter
that
this
mathematically.
later),
and
process. for nozzle
critical
rate
on
within
the
a little
flow
effect
to pt=p,
for a fixed value when
constant The
be
has p'
Pt to pe outside
equal
in
(1-66)
for this part of the remains constant or
a
convergent
critical
static
be discussed
nozzle
remains can
seen
in
pressure
expands
not valid condition
is reduced. flow
is
(in the
flow
equal
in the
which
exhaust
gas
and
greater
thereafter
p',
have
attained
remains
Pt to Pe occurs
are throat
that
We
under these conditions. Thus, flow rate reaches a maximum
the
st)on(is
from
means
exit
Pt still
further?
pressure,
further
in entropy
(p'/p,)
a static
pressure
{ 2-_-_ "_/(_-') \_,+ 1/
The
expands
equations that the
ratios
p,,
nozzle.
process
increase
than
with
p_ is lowered.
critical
below
within
less
becomes
throat
P'=P_'=P'
the
and
nozzle
throat
1 cannot at the
how
(1-29)
p'
where
throat.
if pc is now greater
Assume
velocity)
to pc. As p_ is progressively
increase,
at the
interest.
convergent
static
at the
pe is a little
both
than
previously.
pressure
right
velocity velocity
of most
or outside,
pt is equal
the
1) no matter
(1-62)
pressure
rather
simple (zero
total)
pressure
1 at the
happens
(and
When
case
the
a reservoir
exhaust,
static
as pt.
throat
rate
and
What
the
flow
A2 mentioned
from
The
is the
consider
case
gas a static
temperature
throat)
The
nozzle
the discussion to flow in to the case where the flow
this
first
to the with
is maintained
designated
Once
with
since
us
corresponds is supplied
total)
tions
Nozzles
flow in turbines, we will narrow We will further limit the discussion
entering
(and
concerned
in
pressure
also
remains
upstream M becomes to what condition
state, 1 at value corre-
A nozzle
in 15
TURBINE
this
DESIGN
condition
AND
APPLICATION
is said
to be choked.
Convergent-divergent more the
involved nozzle
case p'
sure
ratio
the
exhaust
commences
the
that
to
the
sonic
T'.
consider
Figure will
the
less
lowest
throat
same
p'
decreases
velocity,
Pt,
and
of the lowered and
(curve
the
this (curve
gas
the throat AD
still
in fig.
at
the
passage (curve velocity
1-3).
I /r
Pe
I I I I I
&
.B
A ,ll
-- _r- .....
B
-_'_"_'_'_
.= N Z
K
H
E
Length
FmuR_;
16
1-3.--Nozzle
becomes
flow
processes.
Note
subsonically
Th roat
-
throat
increases.
velocity
/
If 1-3),
is acting AC in fig.
in fig.
I/
of pres-
discussion.
AB
diffuses
_X._I / rpt
assume
maintained plots
occurring
of p_, the
or Mr----1
than
Again,
showing
supplement than
somewhat
reservoir
1-3,
pressure
value
the
nozzle.
the
the divergent section As pe is progressively
particular
higher
from
length,
p, at the
at some
p_ is still
gas
pe is a little
with
now
convergent-divergent with
nozzle
this case, diffuser.
pressure
us
temperature
pressure
Eventually, equal
and
against
(pt_P_). In as a subsonic 1-3),
of the
to be supplied
at pressure
flow
nozzle.--Let
THERMODYNAMIC
in
the
(with
diveruent
section.
pt:pc._pe),
we
see
to
the
critical
required nozzle achieve If
is less than the critical p_
is
condition only
achieve
a_ain
place
nozzle,
and
the
pendently If
the
divergent
flow
is
part
of the
to discharge
area,
servation
of
relations.
This
shows
flow
isentropic The
supersonic
flow
that
Observing
the
optical in the
means flow.
waves.
Shock
changes temperature process weak.
flow
be
considered
across
Weak
Let
a shock
pressure,
with shocks and
of the that
are shock
complete of pressure
If the
exhaust
pressure
isentropic
and
shock the subsonic
small
some called
the
l)ressure diffusion
AD,
either
fig.
AE,
1-3) fig.
1-3). by
changes flow are
and
the
occur shock
fluid
instantaneously. but,
or
conditions
density in the
even
state Total
though
pressure
there
because
the
Shocks may be strong or flow (and are thus called
velocities small
downstream
angle
oblique
with
shocks), but
of the
respect and
the
the
to
the
velocity
Mach
number
of convergent-divergent
between
at some rises
assume
shock.
p, is reduced
occurs
to
be isentropic.
constant
discussion
ratios
which
allow
(curve
supersonic,
of the
AE,
cannot
is a loss in total
con-
process,
curve
p_ that
thickness,
area
the
Pe_Pt
occurring
remains
upstream
region
nozzle,
at
thus
satisfy
nonisentropic
in subsonic
occur
(and
us now
a normal
(curve
these
the
of throat
unreasonable
Pe_pt
remains
mass
inde-
isentropic by
some therefore,
there
result
for the
D,
is
an increase in entropy. occur normal to the
shocks
downstream than
the 1-3 of
as
the
throughout
values
of very
the
behave
ratio
the
under
are
direction
is less
flow
as
to some
place,
waves
shocks)
shock.
take gas
in static occurs Strong
normal
to
with
and
p_ will
reveals that surfaces of abrupt These apparent discontinuities
may
is a rise
well It
between
is the
As long as the nozzle is choked to
given
in figure
expansion
does
as
isentropic
any
continuously.
diffusion
Thus,
pressure as
critical
exist. value. the
to
throat.
for
exhaust
the throat
constant,
and
then
at
continues
the
energy,
falling
(p'/pe)
the
remains
supersonic one
remain
can
nozzle
is represented
subsonic
isentropic
the
nozzle,
is impossible
ratio
us that
its maximum at the throat,
beyond
and
case
critical
a convergent-divergent
must
showed
state
of
be
only
mass
pressure
that
to
is now
pressure
in
condition
throat
conditions
CONCEPTS
condition
nozzle
throat
(1-65)
part
of the
the
the
constant at is maintained
convergent
throat
condition
critical
the
flow must remain critical condition
FLUID-DYNAMIC
pressure ratio (p'/p_:p'/pc,) required in a simple convergent nozzle.
equation the
the
that
lowered,
where
convergent
Since
the nozzle condition
because
AND
points a little
point
from
below
in the
instantaneously
occurs
D and
the
nozzles
E in figure
the
value
divergent to
shock
plane
at point
part
a value
1-3.
such
to the
of the that nozzle
17
TURBINE
DESIGN
exit.
The
flow
with
AK
being
and
LF
the
to point
the
flow
moves H,
path
the
higher
than
nozzle
exit,
When
p_. In with
from
the
in a nonisentropic
It should do
not
occur
abrupt, tions
may
a shock
1-3
exactly
takes
produce
that
over
from
similar
In
order of
books
and
charts ture.
The
carbon and
general
the
nozzle final
outside
listed
air
and
and
factors
are
of
processes,
however,
are
in reference
and
with
also
the
presented
temperaindividual oxygen,
in references
in reference
the
as
4. These
(nitrogen,
presented
5 include
products 3 and
capacity
are
in
3 to 7.
combustion
and
many
published
as references
air
Charts
calculations, and
products
also
although considera-
downstream
flow
in heat
argon)
proceffects
flow
Tables
its
combustion
vapor,
rise,
real-fluid
in references
of
the
shock
1-3.
and
are
and the
constructed
variation
its
compressible-flow
as functions
for
values normal
of Mach
functions number
effect
and
oblique
a listing
of compressible
tions
in terms
of both
Mach
(TIT',
4
5. The
of pressure,
pip',
are presented
of heat-capacity
sents
18
E.
as
as temperature.
for various charts
the
pe occurs
pressure
Also, subsonic
presented
the
and
presented
to
at point
of p_, the
discussion
in figure
properties
5. Compressibility
Isentropic others)
of
are
water
previously,
the
the
been
of these
include
air
dioxide,
properties well
of
and
pressure
occurs
values
Flow-Function
have
thermodynamic
components
is
cannot
a static
actuality,
and
The
properties
tables
In
thermodynamic
of temperature and
shock
shock
lower
previous
shown and
Some
Thermodynamic functions
exit,
as p_ approaches
distance.
isentropic.
charts
reports.
the
make
to those
and
in
pressure
idealized.
that
to facilitate
tables
For
a finite
Thermodynamic-Property
sets
nozzle
a normal
oblique
static
are
effects
different
qualitatively
process
of pe correspond-
at the
as mentioned
instantaneously
place
flow
the
manner.
out
in figure
shock,
further,
the
value
result
weaker
E,
nozzle-exit
be pointed
shown
and
E,
weaker
isentropic.
expansion
esses
the
and
would
becoming
to point
the
H
and
case,
completely
exit, At some
AKLF,
normal
pe is reduced
will be right
points
shock
p_ corresponds
path
the
is AEH.
strong
this
the
the
being
As
nozzle
shock
nozzle
by
KL
as AMNG.
normal
it is too
is again nozzle
the
such
of pe between
because
is illustrated
diffusion.
toward
in the
values
case
expansion,
isentropic
by a path
ing
flow
in this
an isentropic
shock
represented
occur
APPLICATION
process
being
normal
For
AND
ratio. shock flow
number
in references
Also
included
calculations.
function and
p/p',A/Ac,,
and critical
4, 6, and
are
tables
Reference _hock velocity
and
function ratio.
and 6 preequa-
7
THERMODYNAMIC
AND
FLUID-DYNAMIC
CONCEPTS
REFERENCES 1.
KUNKLE,
JOHN
pressed 2.
Gas
NELSON,
L.
S.j
WILSON,
C.;
AND
Compressibility 3.
ENGLISH,
ROBERT
Properties
of
TN
1950.
KEENAN, JOSEPH Inc., 1948.
5.
HILSENRATH,
6.
HOGE,
KIAN,
YERAM
ties
of
Gases
ties
of
Air,
7.
LEwis
Argon,
and 1955.
Rep.
KAYE,
BECKETT, J.;
AND
for
RICHARD
to
col.
Use
61,
the
no.
New
WILLIAM
W.:
Products
from
BENEDICT,
F.;
NUTTALL,
HAROLD
Carbon 564, Tables,
John
Com-
of
Charts
L.;
for
NACA
and
Sons,
S.;
FANO,
TOULOU-
Thermal
Proper-
Transport
Hydrogen, Bureau
203-208.
° R.
WILLIAM
Monoxide,
and
3500
Wiley
and
National
pp.
Thermodynamic
RALPH
Tables
Thermodynamics
Circular
Equations,
Tables.
W.:
of
300 ° to
W.;
JOSEPH
Dioxide,
ED:
. Generalized
1954,
Charts
CHARLES
of
A.; . .
7, July
Gas
MASI,
NBS
COTA,
JOSEPH:
Tables
STAFF: 1135,
How
WOOLLEY,
Carbon
Steam.
LABORATORY
Functions
AND
AND
1969.
Eng.,
Combustion
HAROLD S.;
F.:
WACHTL,
Comprising
RESEARCH
NACA
and
H.;
E.
D.;
SP-3045,
Chem.
AND
JOSEPH;
LILLA;
AMES
OBERT,
E.; Air
4.
Oxygen, Nov. l,
NASA
Charts.
2071,
SAMUEL
Handbook.
PropNitrogen,
of
Standards,
Compressible
Flow.
1953. COMPUTING
Specific-Heat
STAFF: Ratios
from
Tables 1.28
of to
1.38.
Various NACA
Mach TN
Number 3981,
1957.
19
TURBINE
DESIGN
AND
APPLICATION
SYMBOLS A
flow
a
acceleration, m/seC; ft/sec 2 speed of sound, m/sec; ft/sec
aj
b_ c
c_
area,
m2; ft _
general constants for polynomial, heat capacity at constant pressure, unbalanced conversion
F g h
force, N; constant,
lb 1 ; 32.17
eq. (1-16) J/(kg)(K); (lbm)
(ft)/(lbf)(seC)
J
specific enthalpy, J/kg; Btu/lb conversion constant, 1 ; 778 (ft) (lb)/Btu
M
Mach
M_
molecular
weight,
m
mass,
lb
number, kg;
P
absolute
q
heat
added
ql R
heat
produced
defined kg/(kg
pressure,
by
RI R*
universal
8
specific
T
absolute
t
time,
Btu/lb J/kg;
8314
J/(kg)
Btu/lb
J/(kg
(°R)
mole)(K);
1545
(ft)(lbf)/
temperature,
(K) ; Btu/(lb) K;
(°R)
°R
sec internal
energy,
fluid
V
specific
Ws
mechanical
w
mass
x
length,
in; ft
Z
specific
potential
absolute
velocity,
volume, flow
rate,
of heat
J/kg;
Btu/lb
m/sec;
ft/sec
ft3/lb
done
by
kg/sec;
factor,
system,
J/kg; defined
lb/ft 3
Subscripts: c
critical
state
cr
critical
flow
e
exhaust
t
throat
Superscript: '
absolute
total
condition condition
state
Btu/lb
(M:
(ft)(lbf)/lbm by
at constant
volume
kg/m_;
J/kg;
lb/sec
energy,
capacity
at constant density,
m3/kg;
work
compressibility ratio
90
mole)
(°R)
V
P
lb/(lb
(K) ; (ft) (lbf)/(lbm) force, N; lb
constant,
entropy,
specific
Z
(1-59)
lb/ft 2
J/kg;
friction,
gas constant, J/(kg) frictional resistance
(lb mole)
eq. mole);
N/mS;
to system,
gas
by
Btu/(lb)(°R)
1)
eq.
(1-4)
pressure
to heat
capacity
CHAPTER 2
BasicTurbine Concepts ByArthurJ. Glassman This
chapter
introduces
and
performance
efficiency, nitions,
diagrams,
the
blades
the
end
and
and
blading
of this
chapter.
TURBINE
turbine dimensionless geometry
FLOW
An
analysis
of the
requires
some
through
a turning
directed
parallel
ally
through
gentially
to
tangential radial-axial blade eters.
axis rotating
plane
average) For
indicated
radial
many
types
(or blade-to-blade) values.
Such
of
usually the
and
variation made
at some
third
velocity-variation,
constant
coordinate.
within
system.
For
consists
of one
variation
(rather
are
usually
coordinate
coordinate
directed
tan-
are
the
axial,
Analysis
radial, of flow
of the
desired
ignore
values
the and
as made
in the
flow
t)aram-
circumferential just
use
average
analysis.
or radialthan
and
(or blade-to-
an axisymmetric
diagram,
flowing
one
we can
axial-tangential
a tur-
fluid
circumferentially-averaged
value
calculations
TRANSFER
radi-
2-1.
Velocity
at
directed
planes.
of parameter
in the
GLOSSARY,
coordinate
three
is called
to
one
in figure
axial
of defi-
referring
processes
system and
of calculations,
a calculation
Calculations are
the
means
System
These
form
depicts
ENERGY
of rotation, wheel.
coordinates
in the
coordinate
of rotation,
energy-transfer, by
Terms
energy-transfer
a logical axis
the
defined
Coordinate
and
wheel, to the
the
three
are
convenient
directions
These
flow
flow,
primarily parameters.
AND
Analysis
bine
geometric,
characteristics
tangential
for average well
planes
conditions)
as blade-to-blade
in these
planes.
When 21
TURBINE
DESIGN
AND
APPLICATION
2
Vu
FIGURE
flow
2-1.--Velocity
is predominantly
turbine,
the
nantly
radial,
such
as
in
an
for
a generalized
at
the
is used.
axial-flow
rotor.
inlet When
turbine,
to
a radial-flow
flow
the
is predomi-
axial-tangential
is used.
One
of the
most,
be concerned is the
fluid
tions.
To and
For
flow
interest.
velocity
For
relative
other
a rotating of flow
its variation
in and
to the blade
and
across
row
in a stationary
Diagrams
important in the
the
stators,
across
the
blade.
and
different and
that energy
we will transfer
coordinate in depicting
direcblading
diagrams. the rotors,
In
to be discussed
can be analyzed
flow
analyses
velocity-vector
passage.
variables
of turbine
these
rotating
parameters
and
most,
analysis
we use
and
flow
relative
the
in the
us in making
types, in
Vectors
if not
with assist
shapes
_2
as
plane
Velocity
ered
such
radial-tangential
axial,
plane
components
absolute
velocities
velocities
must
terms
of relative
later
in a manner
in this similar
are
of
be consid-
velocities chapter, to the
and flow
analysis
in
BASIC
Velocity-diagram downstream inside
calculations
of the
the
blade
ferential represent
various
rows.
blade
In
velocity
velocities.
diagram
In making
Relative
the
CONCEPTS
upstream
infinitesimal
velocity
note
and
distances
diagrams,
the
circum-
velocity
absolute
diagram,
velocity=Absolute
locations
considered. The of the flow.
both
velocity
at
or at just
the
are not average
shows the
made
rows
making
variations in flow the circumferential
The
are
TURBINE
and
vectors
the
relative
that
velocity--Blade
velocity
(2-1)
or
W=V--U
where W
relative
V
absolute
U
blade
Since
velocity
consider
vector
velocity velocity
blade
vector vector
velocity
the
is always
magnitude,
in the
that
is,
velocity
shows this
the
diagram components
velocity
absolute
in figure
diagram
and
relative
tangential
the
W= The
(2-2)
blade
speed.
we need
So,
we
can
V--U
2-2
represents
absolute
and
to be
drawn
in an
can
only write
(2-3)
of the
velocities
direction,
be
equation
relative
(2-3)
velocities.
axial-tangential expressed
in
terms
and
also
Assuming plane,
the
of
their
Absolute Relative angle
of flow,
angle of flow, cl7 I I I
V V x = Wx
VU
FIGURE
2-2.--Typical of
absolute
velocity-vector and
relative
diagram velocities
having in
the
same
tangential
components
direction.
23
TURBINE
DESIGN
components
AND
in the
APPLICATION
axial
and
tangential
directions
V2:V_2q-V,,
as
2
(2-4)
Wu 2
(2-5)
and W 2=W2+ where V
magnitude
V=
axial
of V, m/see;
Vu
tangential
component
W
magnitude
of W, m/see;
IV=
axial
W_
tangential
component
ft/sec
of absolute
component
velocity,
of absolute
velocity,
velocity,
of relative
figure
2-2,
m/see;
we see that
m/see;
ft/sec
ft/sec
velocity,
If this diagram (fig. 2-2) were drawn the values marked as axial components From
ft/sec
ft/sec
of relative
component
m/see;
we can
m/see;
ft/sec
in the radial-tangential plane, would be radial components. write
W_,=V,,--U
A
sign
convention
tangential are
of
shown gram and in
components the
exact
in figure shown flow
of
same 2-2.
the
directions,
Therefore,
In
will
for
as
the
velocity
and
diagrams
example the
the
diagram
velocity
dia-
tangential
components
relative
velocities
are
it is not
obvious
that
adopt
and
Wu
the
angles
and
t
24
all
example,
instance,
stick
13_
FIGURE 2-3.--Typical absolute
the
not
shape
Relative angle of flow,
._
for
since
have,
this
absolute and
we
established
velocity, could
2-3.
of
be
geometrical We
in figure
angles
opposite
valid.
must
(2-6)
with
the
equation
(2-6)
convention
is that
r-Absolute angle of flow, cI
Wx Wx = = Vx Vx U
velocity-vector ap.d relative
directed
diagram having tangential velocities in opposite directions.
---I components
of
BASIC
all
angles
and
are
in the
direction
in the we
tangential
direction
can
see
in
a larger
Not
all
Some
the
of a rotor
and
then
negative
with
respect
to the
as we are using. you
aware
valid
for
where
above
at
a location and
direction by
convention Energy
The
basic
tively
as applied of
a
and
to a fluid velocity.
by
any
of the
fluid
at
1 and
2 are
at any
sumed.
Further,
regarded being
as
radii
the
working
with
angles
defined
than
the
else,
all
axial
direction
to use
velocity-
make this
sure
that
information.
turbomachines
Figure
the
2 are
rl and
at
Second
0-0
2-1
the
rotor at
any
the
average
velocity
vectors
of
the
2. The
for
through
and
of steady and
and
directions
angle,
inlet
values
a rotor
rotation
1, passes
point
arbitrary
at
of Motion
represents
axis
r2. A condition
vectors
is rein
Law
at point
is discharged
velocity
representing
inlet
mutually
and
of the
to an
change
axial
bearing have
effect
of the
force,
in magnitude
a radial nents
outlet
perpendicular
in magnitude
the
enters
1 and
at locations
points
state the
the
is as-
outlet
are
of
flow
mass
considered.
The
rise
points
for
with
and
cases.
avoids
in generating
a rotor.
Fluid
path,
all
this
occasion
of Newton's
turbomachine,
angular
rotor
work
Vu Wu.
upstream
directions cases
of for
Transfer
a form
traversing
for
someone
relation
is only
generalized
the the
energy-transfer
simple
convention
have
used
value value
rather
should
velocity
immediately
analysts
if you
the
positive
negative
are
convention,
a negative
In many
generated
of the
small
the
many
tangential
a
U yields
positive
Therefore,
information
are
remains
of
if they
if they
(2-6)
use
Also,
negative this
of a rotor.
values.
are
CONCEPTS
positive
With
convention switch
and
are
velocity.
2-3,
downstream
with
velocity
value
analysts
above
immediately
diagram
figure
of velocity
blade
equation
positive
turbine
use
blade to the
that
shown
minus
of the
opposite
now
diagram
components
TURBINE
any
load. effect
of bearing
tangential
in angular
components axial
must
of the
radial
Neither
the
the
components
momentum
be
taken
velocity axial
nor
angular
motion
It is the
change
of velocity
of the
fluid
and
into
previously.
components
which
on
be resolved
discussed
velocity
friction).
can
through by
The the
a thrust
components the
that results
bearing.
The
rotor
rise
to
compo-
(except
in magnitude
in the
change gives
velocity
corresponds
three
rotor gives
radial of the
the
and
for
radius
to a change desired
energy
transfer. Net outlet
rotor products
torque
is equal
of tangential
to
the
force
difference times
r:(F_r)_--(F,,r)2
radius,
between
the
inlet
and
or (2-7) 25
TURBINE
DESIGN
AND
APPLICATION
where net
torque,
F_
tangential
r
radius,
Applying V=O
N-m;
lb-ft
force,
N;
lb
m; ft equation
at t=O
(1-34)
to V=V
in the
at t=t,
tangential
and
direction,
setting
w=m/t
integrating
from
yields
(2-8)
_w_ Vu F,,--g where w
rate
of mass
g
conversion
flow, constant,
Substituting
angular
(rate
lb/sec
1; 32.17
equation
T =--
Power
kg/sec;
(2-8)
g
Yu,
W
lrl
of energy
into
_
(lbm)
(ft)/(lbf)(seC)
(2-7)
then
=-
w V,.2r2
transfer)
yields
(2-9)
g (V_.lrt--V_.2r2)
is equal
to the
product
of torque
and
velocity: p_r_
J -gJ
w
_(rlV_
.
1--r2V_
,
2)
(2-10)
where P
net
power,
angular J
W;
Btu/sec
velocity,
conversion
rad/sec
constant,
1; 778
(ft)(lb)/Btu
Since (2-11)
roo:V
we can
write p=W
gj
(2-12)
(UIV_.,-U2V,.2)
But P=whh' where
h' is total
(2-13)
into
enthalpy,
equation
in J/kg
(2-12)
(2-13) or Btu/lb.
Substituting
equation
yields
(2-14) J
where
Ah' is here
Equation machines
(2-14) and the
fluid
between
the
two
is the and UV_
t
as hi--h2.
is called
between
26
defined
basic the
the
rotor
terms.
work
Euler must The
equation equation.
for All
be accounted way
equation
all
forms
of turbo-
energy
transfer
for by the
difference
the
(2-14)
is stated,
it
BASIC
can
be seen
that
with
the
energy
fluid
is defined
It is useful will
be
done
turbine and
blade outlet.
There inlet sarily
at the
be made From
for
equation
to transform with
the
the aid
section The
the
be positive
balance,
for a turbine. (1-46),
where
This
CONCEPTS
is consistent
work
done
by
the
as positive.
is assumed or
Ah' must
TURBINE
Euler
along
with diagrams
to be no
radial
same
locations,
equations
in
(2-4)
and
(2-5),
diagrams
locations
This
axial-flow
for
the
axial-tangential
following
three-dimensional
form. an
of velocity
these the
another shows
velocity
component
Actually,
into
which
are
although
radius.
a general
2-4,
the
velocity
outlet
equation
of figure
inlet
planes. at either
are
derivation
not
the
necesalso
can
case. we get
Vx *: V 2- V= _
(2-15)
and Wx_=W*--W,, Substituting
equation
(2-6)
into
(2-16)
_
(2-16)
gives
Vx, 1 = Wx, 1
Wu, 1
Ul
of rotation''e*
Direction V_.
_z E'
,__i/_,,"- Vx, 2 = WX,2
u2
\ '- Vu, 2
FIGURE
2-4.--Rotor
section
with
inlet-
and
exit-velocity-vector
diagrams.
27
TURBINE
DESIGN
AND
APPLICATION
W,_=W*-(V,,-U) Since
Vx=
Wz,
combining
equations
V 2- V,,2=W
2
(2-15)
(2-17)
and
_- V,,2+2UV_
(2-17) -
yields (2-18)
U2
Therefore,
UV,,= 1 (V_+U2-W Now,
adding
subscripts
for inlet
U1V.,,
and
(2-19)
2)
outlet
yields
1 (V_+U2
(2-20)
W2 )
U2V _ _:-21 (W+U_2-W_ _) Inserting
these
values
into
the
Euler
(2-21)
equation
(eq.
(2-14))
finally
yields Ah'--2gJ Equation relation. By
(2-22)
1
is an
(V2
V2_+U__U2_+W2_
alternative
form
Wt2 )
of
the
basic
(2-22)
energy-transfer
definition,
,
,
Vl _
V__
Ah'=hl--h2=hl+-_--h2. Therefore, shows that
comparison
of
2gJ
equation
(2-22)
(2-23)
with
equation
(2-23)
1 Ah:h_--h2=_gj Thus,
the
in static
U 2 and
W 2 terms
enthalpy
change
across
in absolute
of terms transfer.
are
(UI2-U22 of equation
the
kinetic
rotor,
energy
sometimes
tum the
of the rotor.
of this energy
28
that
The
to
in
is actually fluid
flows
a centrifugal
in the
discussion
tangential
force
as
change
acts
V 2 terms
the
change
represent
These
the
three
components
of
pairs energy
of energy
tangential from
figure
2-5
concern
and
the
way
momenthe fluid the
to
cause
in which
the
wheel.
curved on
in the
transfer and
to the the
(2-24)
represent
rotor.
the
momentum
transferred through
the the
2)
Loading
it is the
results
following
change
As the blades,
fluid
while
referred
previously,
(2-22)
across
Blade As mentioned
+W22-W_
passage
it in the
between
direction
each of the
pair pressure
of
BASIC
TURBINE
1
Stations
CONCEPTS
2
sur,_ce J \\1
f
/
/- Suction surface
Flow
"_ ] I
Flow
Axial chord
pll
Pl
m
--P2 Suction surface--,'
Axial distance FIGURE
2-5.--Blade
row
with
surface
static-pressure
distribution.
29
TURBINE
DESIGN
AND
APPLICATION
(concave) surface. Since the free to move in the direction must
be established
through the flow
passage surface.
The
resulting
is illustrated distance. At where the tion value. flowing trailing crease
at
centrifugal
pressure (convex)
the
distribution
to
the
edge.
On
the
below
the
exit
the
of the
blade
surfaces
suction
surface,
pressure
curve
blade-loading
The
the
blade
force
diagram. acting
in the
in a rotating
passage
in a stationary
moving similar
by
is relative
examine
what
through
the
to equation
total
happens
rotor.
through
enthalpy,
to relative
For
purely
rotor
flow,
quently,
no change
constant
for the
We enthalpy. 3O
can
also This
the
changes
axial
stagnation
will
back
up
figure
the
the
often
de-
to the
exit
2-5
curves
blade
is called represents
in a manner conditions
similar
relative
total enthalpy enthalpy.
in a manner
J
(2-25)
in J/kg total
or
Btu/lb.
enthalpy
(2-24)
to
to the
as
we substitute
Now the
let
fluid
us
flows
for W 2 according
we get
we see that the
axial point
direction.
relative total
h '2'-- h ','-Therefore,
the
pressure
be analyzed
If in equation
(2-25),
surfaces
toward
in
considering
passage. Let us first define to the definition of absolute
h"
static
the
reaches its stagnapoint for the fluid
between
h"__h+2_ where
blade
at
Conditions
can
passage
normal to the pressure
the
From
illustrated
Relative
fluid
is plotted against there is a stagnation
increase
tangential
not force
the
lowest
decreases
then
area
turn
and on
blade.
the
and
the
Flow
pressure
sides
pressure. The pressure-distribution
flow
surface
zero and the pressure point is the dividing
two
along
and
force is directed surface. Thus,
in figure 2-5, where pressure or near the blade leading edge
pressure
and, therefore, force, a pressure force
pressure
of static
velocity becomes The stagnation
the
the
path. The the suction
is highest
around
point,
to balance
its curved and toward
in the suction
fluid is constrained of the centrifugal
where flow
speed,
enthalpy
of the
fluid
is a change
in the
blade
speed.
in radius
and,
conse-
is no the
(2-26)
change
relative
total
enthalpy
flowing
remains
process.
a temperature
is called
total
if there
there
in blade
rotor define
relative only
U_-- UI_ 2 gJ
the
relative
that
corresponds
total
temperature,
to relative T".
total When
ideal-gas-law we can write
behavior
and
constant
heat
BASIC
TURBINE
capacity
can
CONCEPTS
be
assumed,
h"--h=%(T"--T)
(2-27)
where c_
heat
capacity
T
absolute
at constant
temperature,
Combining
equation
pressure, K;
(2-27)
J/(kg)(K);
Btu/(lb)(°R)
°R with
equation
(2-25)
then
yields
W 2 T" From and
equation relative
(1-51) total
and
-= T _- 2gJc-_
equation
temperatures
(2-28)
(2-28),
are
we see
related
For
the
rotor
flow
process,
T"--
this
with
we can
equation
2
Therefore,
relative
depends flow
only
through
total
on
blade
that
U_-- V12 2gJcp
temperature, and
(2-30)
T_') shows
T_'--
speed
(2-29)
write
(2-26)
T_'--
absolute
-2gJc_
h_'--h_'=cp(T_'-Combining
the
as follows"
V__W
T'--
that
(2-31)
like
relative
remains
total
constant
for
enthalpy, purely
axial
a rotor.
Relative
total
pressure
brought
to rest
pressure
p. Therefore,
can
be
isentropically
defined
from
as
a relative
the
pressure
velocity
of
W and
a fluid a static
]!
where p"
relative
_,
ratio of heat capacity constant volume
From
this
total
pressure,
equation
and
N/m2; at
crease,
the
rotor
flow
or remain
temperature
and
on
the
pressure
(1-52),
p"
(T"y/(-,-')
process,
constant,
constant
equation
p' For
lb/ft 2
we also
to heat
capacity
see that
=\--_-;,T/ relative
depending losses.
For
at
(2-33) total on purely
pressure the
can
change axial
increase,
in relative
flow,
relative
detotal total 31
TURBINE
DESIGN
pressure it must We
AND
will remain decrease. can
define
APPLICATION
constant
only
a relative
Mach
if the
flow
number
M,_=
is isentropic;
Mr_
otherwise,
as
W
(2-34)
a
and
a relative
critical
velocity
as
Wct=a_.,_=_l
gRT"
(2-35)
where
We,
critical
act, ttt
speed
R
gas
Then, and
velocity,
m/sec;
of sound
at relative
constant,
J/(kg)
in a manner (1-64),
critical
condition,
m/sec;
ft/sec
(K) ; (ft) (lb) / (lb) (° R)
similar
we can
ft/sec
to
the
way
we
derived
equations
(1-60)
get T"T --1+
2--1
M_e_
(2-36)
and T,,--1
3,+1
_
(2-37)
Reaction The
fraction
enthalpy)
that
portant
way
energy
total
of the row.
or more
The
of velocity
across
enthalpy
across
enthalpy
across
enthalpy
the
the
we can
write
stage.
exit
kinetic
energy
stage.
the
rotor,
According
ditions 32
R,tc
is stage
upstream
reaction, and
that
and
the
above
the
change
enthalpy
for static total
absolute
total
in absolute
total
of stage
constant reaction,
(2-38)
subscripts
of the
in
in absolute
hl--h_ --hi
the
of
degree
for classifying
remains
detiIlition
way
is the
change in
cha_lge
im-
kinetic
parameter
change
as the
total
to the
is used
as
in
important cases
an important
of the
same
since
downstream
is one
total
is one
change
in both
is defined
Note is the
absolute
enthalpy
The
Reaction
it is also
R_'_--hl' where
used
as a fraction
stage
in
in static
turbine
and
rotor
the
stator.
a change
a
reaction
tile
(change
the reaction.
diagrams,
across
through
transfer
parameter
simply,
correlating losses. Stage reaction.--Stage enthalpy
by
classifying
a blade
of reaction,
energy
is obtained of
as a fraction
classifying types
of
rotor,
1 and
2 refer
respectively.
to con-
BASIC
The
preceding
equation
for
velocities. Substituting (2-38) yields
equations
can
(U_2--U_ Zero
be positive,
2) and
design.
rotor,
and
be
(2-22)
expressed
and
in terms
(2-24)
into
negative,
or zero,
depending
of
equation.
(2-39)
on the
values
of
(W2_--Wl_).
reaction
stage
can
CONCEPTS
(U?-U22) + (W 2-W ?) V22)+ (U2 U22)+ (W22_W2)
R.,,-Reaction
reaction
TURBINE
is one
important
If Rst0=0, all the
value
there
work
done
is no by
that
characterizes
change
the
a particular
in static
stage
enthalpy
is a result
in the
of the
change
in
absolute kinetic energy across the stage. This stage is called an impulse stage. In the general case where the fluid enters and leaves the rotor at
different
of static effect
radii,
an impulse
enthalpy and
an
in one
equal
relative-velocity
stage
direction
change
effect.
other
purely
pressure
people
define
in the
rotor
definition
impulse rather
in terms
of static
used herein. The definitions exactly
difference coincide.
Simple
examples
windmill, from
or the
a stationary
the lawn rotation.
develol)ed
energy
at the
that
blade
kinetic
energy
blade-row stage For
the
blade-row row.
For
the
blade
exit.
These
a
corresponds
reaction
represents
no
are by
the the
in
static
isentropic
child's
This
same
as that flow,
pinwheel,
impingement
example
Thus,
enthalpy. the
For
in static only.
change
in static
the
the
of a fluid
of a reaction
turbine
from
reaction
is
defined
as
the
kinetic
as a
fraction
of
the
kinetic
are
stator
or
to the
change
an effect
the
kinetic
axial-flow
energies
rotor,
in static similar
thus
is
water
row
nozzles,
the
the
enthalpy. to that
causing
relative change
in
Therefore,
represented
by
reaction. a stator
blade
row,
R,,
where
turbines
(U 2) by
change
velocity
of
to losses.
A simple
within
centrifugal
any
basis
operated
ejects
the
a change
contributed
flow,
change
having
is approximately
is due
wheel
that
no
reaction.--Blade-row
energy to
than
by
of relative WI= W2.
the
pressure
nozzle.
sprinkler
Blade-row
on
of impulse paddle
from
direction
axial
enthalpy must be caused by a change an axial-flow impulse stage must have Some
result
contributed
in the
For
may
Rs, is stator
reaction.
reaction
is defined
V1_-- V°2----1 V12 For
a rotor
as
V°2 Vl 2 blade
(2-40) row,
reaction
is defined
as
33
TURBINE
DESIGN
AND
APPLICATION
R
--W22--W1_= to--
where
R,o is rotor
tions
upstream
stream
some
reaction. of the
of the
In
rotor,
The
the of
kinetic
equations
(2-40)
and
(2-41)
rather
than
all adiabatic
velopment when
the
presented this
gas-law shown
work)
and
veniently
temperature entropy
for
down-
later
lines
all
the
velocities
similar
appear
to the
energy
trans-
maximum or
energy
pressure
do it here),
transfer
ratio from
and
Therefore,
variables
pressure.
is obtained
the With
with
Since
previously
and
as can
ideal-
previously by temwe
actual
entropy
the
temperature,
of interest,
pressure,
(de-
we will illustrate
discussion.
(isentropic)
decreasing
to
V2).
can
diagram. against
increases be seen
Constant-entropy-
b.-
E Pl > P2 > P3 E b--
I Entropy, s
FIGURE
34
2-6.--Typical
temperature-entropy
diagram.
con-
expansion
means of a temperature-entropy diagram is a plot of temperature and
of
is
be proven
in this
being
of constant
temperature
terms
assumptions, we have changes can be represented
ideal
by
in
Process
a given can
changes.
the
processes in a turbine The temperature-entropy entropy
for
we will not
a little
represent
increasing
to condiand
definition than
energy)
This
constant-heat-capacity energies and energy and
pressure,
kinetic
is isentropic. (but
the
processes,
of mechanical
graphically
peratures
2 refer stator,
is defined
V rather
Expansion
of
and that
of the
that
(i.e.,
expansion
equations
fact
0, 1, and
This
except
squared
(development process
(2-41)
reaction
energies.
Turbine For
W22
downstream
blade-row
instead
formation
W12
-
respectively.
literature,
power
l
subscripts
stator,
velocities first
W22
with from
BASIC
the
discussion
chapter
1,
example by
entropy,
the
For
the
These The the
coastant-entropy-1)rocess
figure
pressure
purposes four
four
the
A
At
diverge;
is also
diagrams
the
with will
like
process
values
of
therefore,
at
difference
in
looks
the
is repre-
temperature
and
increasing
values
between
any
two
increasing.
of clarity, steps,
diagram
constant-entropy
temperature
CONCEPTS
thermodynamics T-s,
increasing
curves
curves
into
or
2-6.
line.
entropy,
pressure
divided
in
a vertical
constant
given
the
temperature-entropy,
shown
sented of
of a
TURBINE
each
then
be
turbine shown
expansion
process
in a separate
combined
into
T-s
a single
four diagrams represent the stator expansion process relation between absolute and relative conditions
will
be
diagram. diagram.
(fig. 2-7 (a)), at the stator
P()"P'Lid
_,,_Jc-T_= T_
Ti
TO
Tj'
------7
vl p?
T1 Tl, kJ
T1
NJCp 0 (a)
(b)
i.--
p_
P_' T_'
/
/
Ti' : T_'
T_ 2gJcp
P2
>2gJCp
hl--_
T2
CPl
T2 ....
(c)
(d)
l Entropy, s
(a)
Expansion
process
across
stator.
(b)
Relation relative
(c)
Expansion
process
across
rotor.
(d)
Relation absolute
FIGURE
2-7.--Temperature-entropy flow
diagrams turbine.
for
between conditions
absolute at
stator
between conditions
flow-process
and exit.
relative at steps
and
rotor of
exit. an
axial-
35
TURBINE
exit
DESIGN
(fig.
blades
2-7(b)),
(fig. at
Figure
APPLICATION
the
rotor
2-7(c)),
conditions four
AND
and
the
rotor
2-7(a)
shows
before
is represented
point
and
the
the
expansion
indicated state
by
process
by
the
small
by
the
1 with
arrows. actual
It
related
gies
and
The represent If the
static
For
and
were
rotor
exit
process
The
is shown
four
state
as
the
enthalpy (p_,
figure
2-7(c),
it is on
for
the
T2._d), state refers
figure
2-8,
the
entire
stage
36
figure
the
and
by
the
the
which the
ideal
rotor
in
kinetic
in figure
en-
2-7(c)
in
curves
before
and
so
that
would
be that
and
after
the
T;'=
T_'.
indicated
are
is on
the point
ideal 2,id and
absolute
now
are
right state
!
line.
rotor).
The
the
one by
In
figure.
figure
ideal
l_,_t_fing
the
stage
diagram total
the
being, Note
arrows
ignore
the
that
the
line 2-8, the
rotor
alone.
of the
across subscript
in
where
2-7(c),
expansion
the isen-
relative
in figure
across
to the
at
constant-entropy
as in(licated
expansion refers
time
of the
at
into and
indicated
the
ideal
related
energies
total,
an
states
are
combined
For
developed by
total
states
kinetic
expansion on the
energy
developed
These
points.
same
kinetic be
absolute
0 constant-entropy the
relative
absolute
2-7
indicated
stator
relative
assumed, state
would
static,
turbine
subscript
final
2-7(d).
state
to
(both
is
relative
The
the
is not
2,id
by
developed
constant-pressure
flow
the
appropriate
script
that from
figure.
is shown four
pressures
than
of figure
2-8.
rotor
the
that
relative
differences
point
be
proceeds energy
and
total
is less
in
diagrams figure
processes
through
would
If
The actual process proceeds from state 1 to the small arrows, with an increase in entropy.
between
tropically, and the exit are indicated. shown
state
(1-51).
through
in the
The
axial
be noted
it can
process. The relation
static
developed
flow
at each
as indicated
kinetic
absolute
the
isentropic,
Here
actual
the
relative
2,id. by
again
state
process
be
analyze
across
simplicity,
expansion
the
would
conditions.
by the subscript state 2, as indicated by
the
in entropy,
are indicated
process relative
the
expansion.
and
temperatures
of the
than
The total
energy
equation
final
the
stator.
conditions. Figure 2-7(b) shows the relation between relative total states at the stator exit. These states
expansion
terms
with
the
that
we
isentropica]ly, total
absolute
absolute
between
actual
increase
be noted
the
and
kinetic
distance
The
a small
previously,
terms of relative the absolute and
static
The
isentropic,
is less
moving
and
across
the
in accordance
1,id.
can
process
process. As mentioned
are
vertical
were
to the
relative
process
expansion.
point
subscript
0 to state
the
the
state
between
represent
the
relative
2-7(d)).
expansion
after
total
process
relation (fig.
curves and
state
the
the exit
constant-pressure
pressures
expansion
subIn the 2,id
BASIC
TURBINE
CONCEPTS
T_" T_ i1
ii
P2
=__Po
To
Ah'
(h6-
T_? '_ T_' p-
Ahid
\ lh
T1
--
--j,,J
T_ Ca
E
I
T' 2, id
Ahid (h 6 " h2, id )
T2 TZ id
Entropy, FIGURE
is,
2-8.--Temperature-entropy
therefore,
diagram
ambiguous
obvious
from
process
(as represented
be obtained To-- T;. ,d).
figure
but
2-8 an
for
the
work
T o-
ideal
T_)
Since
turbine
used actual blade
for
blade
to express this
rows
is less
purpose
in both from
the
the
work
than
process
operate
performance.
is blade-row
exit kinetic energy row. For the stator,
axial-flow
(as
turbine.
senses. real
It
that
could
represented
by
isentropically, One
efficiency,
divided
by the ideal
common
which exit
we
need
is defined
kinetic
_
is stator
indicated in figure (1-55), we get
efficiency. 2-7(a).
The By
as the
energy
of the
For
the
(2-42)
relation
applying
between
equations
V_ (1-51),
and
where
is
and
(2-43)
rotor
Wi _'°=W_, ,d Vro is rotor
is indicated
2 Vl._a
(1-52),
\pod
L
a
parameter
V_I
where
is
turbine
Efficiency
do not
blade-row
of an
used
obtained
turbine
Blade-Row
parameter
a stage
is commonly
that by
from
s
in figure
efficiency. 2-7(c).
The For
(2-44)
relation
purely
axial
between
W_
and
W_._d
flow,
37
TURBINE
D]_SIGN
AND
APPLICATION
W_,,d=2gJc_,T;' Thus,
with
inlet
it is possible
conditions
and
to calculate
Blade-row
in
as a loss rather
known
for a given
for a specified
terms
than
(2-45)
j
efficiency
exit velocity
performance
expressed
1-\-_,/
of
blade
exit static
kinetic
energy
as an efficiency,
is
sometimes
as
e=l--n where
e is the
kinetic-energy
Blade-row total
differing by dimensionless. actual
also
Several the
(2-46)
loss coefficient.
performance
pressure.
can
be expressed
coefficients
of this
normalizing parameter Inlet total pressure, exit
dynamic
head
have
all
been
in terms
type
used ideal
used
have
this
Axial
I
/I
f
f
!
Y,
Y',
ff
!
between
the
pressure
Y"
Y"o
stated,
and
they
are
total-pressure
can
be derived.
loss
involve
I¢
t!
p2
process
or stage
energy
is isentropic.
Since
parameter that
for expressing
we use
ratio
is the
of actual
This
Overall stage or
stage
to
turbine
we
are
It is the the
ideal
or stage
discussing
process
inlet
transfer condition
aerodynamic
when
simply
which
refers energy
energy
based to
efficiency
the
exit and
transfer. The
definition
are
overall
transferred on
turbine
in the
isentropic pressure. are
as the
efficiency.
above
to the
a
parameter
is defined
or adiabatic the
expansion we need
The
(isentropic)
apply
the
isentropic,
performance.
isentropic
efficiency energy
total-
are not
dependency.
efficiency,
of actual
various
relations
is never
or stage
that we can to follow. ratio
the
Relations
Efficiencies
to ideal
as the
coefficients.
is maximum
or stage
e_ciency.--Overall
process.
the
38
the
transfer
ways sections
Stage
transfer
turbine
is known
several different discussed in the
and
turbine
energy
efficiency
number
(2-47c)
--P2
and
These
(2-47b)
P_
loss
coefficient
a Mach
Turbine Turbine
_f
P2
kinetic-energy
loss coefficients
(2-47a)
,, yT o__P, p_ --P2 --p_
"Po--Pl
and
It
--P2,,
'
• 't--P--_--pl
where
as follows:
PI
Po--p___._ "--P;--Pl
V"
each
the coefficient head, and exit
purpose
YTo-_P-'
Po
v'
used,
in
rotor:
t
po--pl,
of a loss
been
to make dynamic
for
Stator:
y,
row,
pressure.
not,
or
turbine
flow
from
Note
that
at
present,
BASIC
considering seal friction.
mechanical
We will turbine.
define
This
however,
Actual
absolute
total
in figure
2-8.
Now
work
energy
transfer
energy
for conversion conditions are used.
If
plenum, energy
turbine
then
the
could
shaft for
the
work the
in the
down
If we were the
kinetic
loss.
The
are
carried
shaft
to the
exit
ideal
case,
energy kinetic
work.
the
cases
where
pose,
the
entire
from
the
exit
case
is the
high
velocity
leaving
and
effi('iency exit
total
before turbine exit
based by
the exit total kinetic energy)
is always
between
the
two
the
ideal is
situation,
obvious must
as a
wasted,
but
of its exit
to static
of their
serves
of ideal
a useful work
exit pur-
computed
example
of this
be expanded
therefore,
In exit
converted
basis
most and,
not be
basis the
basis
engine, ideal
ideal
enthall)y
2-8.
It
can
must based
higher increasing
than
work
available
is culled
work
called
con(tition than that
efficien('y
are
the
gas
to
the
above
may
the
state
be considered
energy
the
equal
in tile
on
static energy.
would
The
Here
exit
to
exit. kinetic
stages on
converted
a high
to
a
velocity
a waste.
on
on the the
on
the
kinetic
desirable
they
rated
kinetic
('.on(litions
conditions in figure
are
conditions.
based static
the
as in a
wasted
been
would
other
is rated
the
zero
where
stages
leaving
inlet,
is available
be
state
stage
the
turbine.
have
turbine
stage,
stage
is not
the
This
it would
with
last
is rated
state
available
is dissipated,
we use
total
turbine-exit
turbine total
rel)resented in(licated
last
the
efficiency
total
next
other
jet-engine
the
The
the
the
leaving
to the
Thus,
state
a multistage
energies
over
energy At
in
is indicated
energy
wasted.
because
exit
only
the
decrease
this
ideal
energy
a case,
work
the
from
by
l)lus exit kinetic
and
kinetic
if it could
such
static
considering
the
is just
1)ut to use In
done
occasionally,
is the
conditions.
kinetic
of ideal
work
and
At the turbine or stage exit., static and total conditions are sometimes
energy
turbine.
condition, while total conditions. In
been
as bearing
work
or stage,
inlet
CONCEPTS
people;
herein
or total
work. used
shaft
as shaft
to define the
such
most
defined
turbine
exhaust-flow
have
this desirable static state.
the
exit kinetic
computation
expand
as
because
to shaft sometimes
by
is defined
of static
used
as the
used
whether
basis
is ahvays
to items
transfer
across
consider
due
one
transfer
enthalpy
on the
state
energy is the
we must
to do total
actual
definition
actual
energy.
inefficiencies
TURBINE
available tile be
the
between
the
inlet
efficiency.
The
decrease
for each
of these
that
the
be less (as long on the exit static static
efficiency, increasing
ideal
with
inlet The
total
and
conditions
work
as there condition. exit.
the
efficiency.
total seen
with
between
static
cases
are
based
on
is some Thus, the
kinetic
exit total
difference energy. 39
TURBINE
DESIGN
Overall
AND
turbine
APPLICATION
efficiency
_ and
similar equations. The inlet and exit conditions,
subscripts instead
stage.
static
Overall
turbine
stage
efficiency
_tg
are
defined
by
in and ex are used to denote turbine of the subscripts 0 and 2 used for the
efficiency
can
be expressed
as
(2-48a)
For the ideal-gas-law reduces to
and
constant-heat-capacity
assumptions,
this
T',.--T',_ V
/ p,, \(_-l)/_l
Overall
turbine
total
efficiency
(2-48b)
J
T;. is expressed
as
hh' h;.--h',_ _' = .-_-7-, =h' _'
For the ideal-gas-law reduces to
and
constant-heat-capacity
._, _
total
and
appropriate Relation
of turbine
efficiencies
are
(2-49b)
similarly
defined
but
with
the
as
However,
to stage
a measure
it is not
efficiency.--The
of the
a true
overall
indication
overall
turbine
performance
of the
of
efficiency
the
of the
comprising the turbine. There is an inherent thermodynamic hidden in the overall turbine efficiency expression. If equation
(2-48b)
or (2-49b)
a given
stage
which
were
pressure
for a stage
ture
would
gas
entering
2-8,
the
losses
perature stage though
for a stage,
and
stage
the of one
For
stage
appear
the
following
is then
capable
of
delivering
all the
individual
overall
turbine
the
number
of stages.
effect such
can as
stages
efficiency be shown
figure
2-9.
by The
the
a turbine, in the
stage have
del)ends
means solid
to
form
on
the
same the
line
transfer, teml)era-
of a higher
pressure
O-2,id
tem-
following
Therefore, stage
of a temt)erature-entropy verticnl
for
be __een from This
work. the
that
energy
as can
(T_T2,_,).
additional may
still
be seen
is prol)ortional
stage.
entering
it could
efficiency,
be (To--T_),
gas
the
This
written ratio
of the
figure
4O
[1 --\p_--_-/ (P-_= _('-'>"]
e3_ciency
is useful
turbine.
gram,
this
subscripts.
efficiency stages effect
static
assumptions,
T'_.--T',_ T_
Stage
(2-49a)
even
efficiency, ratio
and dia-
represents
BASIC
TURBINE
CONCEPTS
Pk k
_ \\
1
i '
b---
E
\\ A,'i .,tg
\
¢D
E
_\
¢D b--
Ahld:stg
\I:
\\
Ahld, stg
2,id
Entropy, s 2-9.--Temperature-entropy
FIGURE
isentropic
expansion
dashed
line
taking
place
The
0-2
from
obtained
ideal
work
difference
of temperature
increasing
p_),
the
that
represented
greater
by
constant E-F
stage
is greater
ing
the
the
sum
which and
by
virtue
ideal
Thus,
the
than work turbine
the
the
of
actual
work
B-2,id.
With
lines
three
stages,
it can ideal
be seen work
that
the
0-A,
work
where the
increases
stage
(p_
is greater for
this
stage
be greater.
C-D,
and
and
to
than stage
an(l,
is for
Similarly,
E-F
represent-
2; Ahld. stt representing
Z Ah;dstg
represented
second C-D
previous will
_' _'sto.
previously, pressure
the
line
The
efficiency
is ,7_tg Ah_,.stt,
isentropic
for
the
for the
p_.
efficiency
mentioned
of constant
by
inefficiency
efficiency,
of these,
is the
A-B.
of
pressure
stage
stage
Hence,
represented
in a multistage
turbine
same
As
lines
of entropy.
work
each
a stage.
between
values
isentropic
the
effect
exit
of overall
having
from for
reheat
Po to
process
each
work
the
showing
pressure
the
stages,
Ah_d. stg is with
inlet
represents
in three
actual
diagram turbine.
by
is greater the
sum
than of 0-A,
A-h_, A-B,
B-2,id. 41
TURBINE
DESIGN
The
total
to P'2 can these
two
AND
actual
APPLICATION
turbine
be
represented
values
must
work
obtained
by
either
be equal.
from
7'
the
expansion
Ah',d or
_tg
from
Z Ah'_.,t,,
Po and
Thus,
-'Ah'
'
(2-50)
z ah,_.,,, Ah'_
(2-51)
or
, _-_
Since
2_ Ah'_d,s,g
greater This
than effect
be confused between
_Ah_d,
with
the
stages,
The
of
efficiency
turbine
process
which
equation
stages
the
overall
isentropic
efficiency
the stage isentropic efficiencies, or _' _tg. in turbines is called the "reheat" effect. is also
for
constant
of adding called
calculating stage
heat
from
This
an
is
must
external
not
source
"reheat".
overall
pressure
turbine
ratio
efficiency
p_/p_
and
for
several
constant
stage
_t_ is
I--
-,
1--_,t_
J)
1--\_-£]
_1 --
(2-52)
( p i t nt(.y_ l)l_, ]
1 --\_oo/ where n is the number be found in reference The
fact
on the
that
stage
pressure
ratio,
of turbine
efficiencies
not
comparison
a true
higher
pressure
sirable
to be able
In
order
ciency
ratio
of stages. efficiency raises
from
machines
of their
to express
temperature
(T--dT),
by
a true
all reheat
the
consideration.
can
this
a gas where
efficiency
from
is expanded d T is the
we
It
have
ratios
is
as the
one
would
be
of de-
for a turbine. to be the
effi-
stage.
of isentropic
definition,
A comparison
effect. would
depending
pressure
behavior,
reheat
aerodynamic effect,
small
suppose stage
equation
efficiency,
of different
eff_ciency.--Starting
T,
of this
turbine
aerodynamic
is helped
Infinitesimal-stage
tropic-efficiency
derivation
an important
of an infinitesimally
infinitesimal
differs
of two
to eliminate
temperature an
The
1.
pressure
to pressure
increment
efficiency
p
(p--dp)
of temperature
vp. By
using
the
and and for isen-
write
d T = _pT E l --(ppdp
) (_- ' ) /_]
(2-53)
and dTT_ _1o[1--(I 42
__)(_-
z,l_]
(2-54)
BASIC
These
equations
efficiency
the be
the
the
be
than
static
rigorously
authors
the
in accord
ignore
proportional
the
to the
that
stage,
there
temperature
fact
that
the
is used
isentropicactual
in
the
work
differenOther
in kinetic
d T'----d T. However,
that
the
differential.
is no change
so that
with
CONCEPTS
total-temperature
static-temperature
assumption
infinitesimal
quite
Some
should
rather
make
not
definition.
differential tial
are
TURBINE
authors
energy
it ahvays
across seems
to
infinitesimal-efficiency
expression. Using
the
evaluation
series
expansion
of equation
approximation
(2-54)
(1-#x)
n= 1 +nx
dT 7_1 dp T --_ 7 I' Integrating
between
the
for
yields
turbine
inlet
(2-55)
and
exit
yields
Tfn
In _(2-56) z/P--7--
1 In p_" "Y
Equation
(2-56)
The
can
infinitesimal-stage
dynamic
efficiency,
efficiency
is also
from
method
the
constant, called
be written
where
we get
for the
as
efficiency exclusive
known
as the
n is called l)olytropic
the
effect
l)olytropic an
the
process.
_p is SUl)posedly
of
of expressing
a l)olytropic
Pex
of
the
efficiency.
irreversible
polytropic
for
This
process
exl)onent
Substituting
true
aero-
ratio.
This
name
arises
pressure
v from
path
as pv"=
, and
the
process
the
ideal
gas
process
{p,n'_
T,n
(n-l)/n
(2-5s)
\p,,! Equations process relate
(2-57) were
l)olytropic
and
(2-58)
to be expressed efficiency
are as
and
the
n
inlet
and
exit,
very
similar,
a ])olytroi)ic
n--1
If we neglect
is law,
polytrol)ic
and
if
the
process,
then
exponent
as
-),--1
turbine we
couhl
(2-59)
?
kinetic
energies
for
the
overall
turbine 43
TURBINE
DESIGN
process,
we
ciency.
Actual
AND
can
APPLICATION
relate
turbine
temperature
overall
efficiency
could
be expressed
drop
T_ _Te_='_T_,
to
E1 --\_-_,/ (Pe_ y"-l)/_
(_-e_)
1J
_'{(_-
1)/_]
L -\_/ Equating
(2-60)
with
(2-61)
then
(2-60)
k
(2-61)
J
yields
_=1--\_/
This proach
relation
is illustrated
each
other
unity.
However,
ciency
levels,
as at
the
two
in
(2-62)
figure
pressure
higher
effi-
as
or _1
polytropic
2-10.
ratio
and
pressure
efficiencies
can
The
two
efficiency
ratios,
especially
differ
signiticantly.
efficiencies each at
ap-
approach lower
effi-
.9-Turbine pressure
¢-
_.,,_
r_tio /.,///
09 ----
.8
B
b---
.5
1
I
.7 Turbine
FIGURE
2-10.--Relation
between Specific
44
I
,8 poly_ropic efficiency,
turbine heat
overall ratio
I
.9
7,
ffp
and 1.4.
1.0
polytropic
efficiencies.
BASIC
DIMENSIONLESS Dimensionless turbine
number introduced
of
the and
dimensionless
serve
geometry,
and
to correlate
Dimensional
analysis
variables the
or
minimum
more
the
analysis
that some
of the
procedure
variables for
and
obtaining
flow
yields
The
dimensions, term
resultant
ratios
implies
the
actual
insight
that
into
shape
and linear
]'his
based
on
on
is an
various
These viscous
a basic
ideal attributes
include
effects;
an elasticity
number),
which
number, pressing are
the The
matic, similitude.
which real
parameter
effects,
significant concept and
fluid,
ratios
which which for
for gas groups leads conditions
the
Reynolds
and
based
relations.
the
effect
of
surface-tension to the
and Of
analysis
ideal
reduces
effects;
change of the
an
expresses
a gas
than
groups,
expresses
effects. the
of
modify
of
geometrical rather
dimensionless
that
gravitational
quantities operating
physical
is a con trolling
characteristic other
in general,
of dimensionless two
are
(which
parameters
dynamic If
by itself,
compressibility
expresses
fluid
dimensions),
number,
expresses
formal
of fluid
basic
The
of linear
of
1, which
represent
dimension
number,
Weber
of the
of a
pertinent
problem
of velocities.
parameter
There
Reynolds
the
nature
The the
the ratio of the force due to the inertia force due to the motion
of a real
the
forces;
flow
fluid.
general
states
powers
reference
terms
ratios
(as a ratio
of each
factor. Another term expresses of pressure in the fluid to the fluid.
the
dimensionless
of forces,
magnitude
to the
and
form
of
group.
including
analysis
which
from
be
of dimen-
in the
groups
con-
once
basis
product
a dimensionless
the will
at least
7r-Theorem, a
some
each
groups
The
be expressed
in many texts, this discussion.
considerable
relations.
may
groups,
them.
is the
throw
for grouping
variables
dimensionless
of dimensional
are of
use
of variables
they
of such
representing
forming the
variables is presented served as the basis for Application
all the between
equation term
a group
so that
number
1)rocedure
each
allows
of dimensionless The
relation
physical
A
parameters for the
It is a procedure
to include
as a formal terms,
that
to be arranged
number
physical
a complete of
performance.
Analysis
relation.
variables.
necessary
to represent
number
of the
a smaller
two
sional
relation
nature
into
taining
diagrams,
analysis.
is a procedure
a physical
on the
velocity
turbine
is dimensional Dimensional
light
classify
more commonly used dimensionless discussed in this section. The basis
parameters
comprising
CONCEPTS
PARAMETERS
parameters
classify
TURBINE
the
these
Mach Froude
terms
Mach
ex-
numbers
flow. as ratios _o are
the such
of geometric, idea that
of
kine-
similarity all
the
or
dimen45
TURBINE
DESIGN
sionless
terms
of the
separate
obtained.
AND
have
APPLICATION
the
same
variables,
Complete
value,
then
physical
similarity
is ever
be approached
of similarity
the
to the
operation
rather
full-size
at some
Another fluid
design
Turbomachine Application flow
in are rows
the
use
in conjunction
_4th
size,
following variables tant relations : Volume
flow
Head,
to the
rate,
P,
Rotative
speed,
set
to ideal and
Q, m3/sec
or ft3/sec
parameters.
These
and
of the of the
power
fluid.
more
The
impor-
W or Btu/sec N,
rad/sec
or rev/min
Fluid
viscosity,
u, (N) (sec)/m
Fluid
elasticity,
E,
dimension,
variables,
the dimensional five
capacity, 3, which
D, nt or ft
_-or lbm/(ft)
N/m 2 or lbf/ft five
dimensionless
or flow is called
_2_' rate, the
groups
constants groups
can
in order
can
be formed.
to ease
be expressed
p-N3D 5' is exl)ressed capacity
(sec)
2
dimensionless
conversion
_fcn
Q/ND
of fluid
flow rate,
some
p, kg/m 3 or lb/ft 3
The
work),
to demonstrate
density,
the
problem
operational characterin the relation of head
used
Fluid
lation,
of
properties
linear
drop
involves conditions
or (ft)(lbf)/lbm
speed,
these
results
detailed examination of flow within In addition, dimensional analysis
Characteristic
From
46
relates
so that
the
ambient
general
the
are
H, J/kg
Power,
this
scale
with
Parameters
has great utility in the analysis of the overall istics. For any turbomachine, we are interested flow,
use
of similarity
at or near
mentioned
important for the of turbomachines.
(for compressible
it
One
condition.
analysis
previously
linear
the ratios
purposes
utility.
performed
Operational
of dimensional
results
parameters the blade
be
with
the
similar-
the ratios complete
practical
of smaller
can
are
are everywhere the velocity
for most
machine.
severe
(1) geometric
to be of great
of models
of machines
than
but
experiments
values
conditions
which means that is doubtful whether
closely
operation
inexpensive
applicable
attained,
sufficiently
is the
relatively
implies
similarity, same. It
individual
physical
dimension ratios which means that
are the same; and (3) dynamic of the different forces are the can
of the
similar
similarity
ity, which means that the linear same; (2) kinematic similarity,
physical
regardless
exactly
u
the
manipu-
as
(2-63)
' pN2D2/ il_ (limensionless
coefficient.
If we
It
can
form be
further
by
BASIC
rel)resented
TURBINE
CONCEPTS
as Q
VA
VI) 2
V
V
(2-64)
Thus, the capacity coefficient is equivalent to V/U, and a given value of Q/ND 3 implies a l)articular relation of fluid velocity Io blade speed or, in kinematic terms, similar velocity diagrams. The head is expressed in dimensionless form I)v H/N21) ', whi(,h is called the head coefficient. This can be rel)rcscnted as H H N 2D,_a: -_
(2-65)
Thus, a given value of t./N2D 2 iml)lies a particular rclatiol_ of hea_l to rotor kinetic energy, or dynamic similarity. The term P/pN3D 5 is _t power coefficient. It represents the actual power And thus is related to the capacity and hea(t coefficients, as well as to the efficiency. The term pND2/u is the Reynolds number, or viscous effect coefficient. Its effect on overall turbine 1)erformance, while still iml)ortant, can be regarded AS secondary. Ti_e Reynolds number effect will be discussed separately later in this chapter. The term E/aN2D 2 is the compressibility coefficient. Its effect depends on the level of .XIach number. At low NIach number, where the gas is relatively incoml)ressible, the effect is negligible or very secondary. As NIach number increases, the compressibility effect becomes increasingly significant. Velocity-Diagram
Parameters
We have seen that the ratio of fluid velocity to blade velocity and the ratio of fluid energy to blade energy are inq)ortant factors required for achieving similarity in turbomachines. Since completely similar machines shouhl perform similarly, 'these factors become iml)ortanl as a means for correlating performance. Since the fa('tor._ I_/'U aud H/U z are rclatc(I to the velocity (liagrams, factors of this type ar(, refcrrc(I to as velocity-diagram I)aramcters. Several velocity-(liagram parameters are co,mnonly us(,_l ill t_,rt)illc work. NIost of these arc ,ise(l I)rim'trily with rcsl)e('t to axial-ttox_ turbines. One of these parameters is the speed-work parameter X::-
U 2
(2-66
gJ/W 'Fh(_ re(:ipro('al
of the sl)ce(l-work
parameter
is also oflcn
use_l, aml
it 47
TURBINE
DESIGN
is referred
For
AND
to as the
an axial-flow
APPLICATION
loading
turbine,
factor
or loading
1 ¢=X--
g JAb' U2
we can
coefficient
(2-67)
write
(2-68)
Therefore,
equations
(2-66)
and
(2-67)
X=
Another
l)arameter
often
used
1
can
be expressed
as
U
(2-69)
¢--AV_ is the
blade-jet
speed
ratio
U p_
where
V_ is the
or spouting,
jet,
or spouting,
velocity
is defined
ideal
expansion
stage
or turbine.
from
inlet
That
(2-70)
"_fj
velocity, as the
total
in m/see velocity
to exit
or ft/sec.
The
corresponding
st, atie
(:onditions
across
of equation
(2-71)
back
into
(2-71) equation
(2-70)
yields
U _= -7-= _ 2gJAh,d A relation
between
parameter the
static
can
the
be obtained
efficiency
the
is, Vj2= 2gJ,_h,,_
Substitution
jet,
to the
blade-jet by
(2-72)
speed
ratio
use of equations
and
the
(.2-66)
and
speed-work (2-72)
and
definition zXh'
The
resultant
This
shows
must
also
is directh speed
ratio
Another 48
relation
that
if efficiency
be a function related
onh
n =Sh-_
(2-73)
v= _/____ _
(2-74)
is
is a funclion
of the
other.
to the
is related
to the
frequently
used
actual
velocity
of ()ne of these
While
the
veloc)tv diagram
velocity-diagram
parameters
speed-work diagram, and
to the
parameter
it
parameter the
blade-jet
efficiency. Is
the
flow
BASIC
factor,
or flow
TURBINE
CONCEPTS
coefficient
(2-75) The
flow
coefficient
can
be related
to the
loading
coefficient
as follows:
v, / v, By
using
equation
(2-69)
and
the
velocity-diagram
_=#
cot
(V,,. ,'_ al kAVu /
The term Vu. I/AV,, cannot be completely specific types of velocity diagrams, such next
chapter,
(a different each can
this
term
function
of the
becomes
for each
different
be expressed
types
of the
(2-77)
of loading
of velocity
of velocity
in terms
we get
generalized. However, for as will be discussed in the
a function type
geometry,
coefficient
diagram).
diagrams,
Therefore,
the
loadingcoefficient
alone
flow
and
for
coefficient
the
stator
exit
angle. It
is thus
related
seen
to each This
next
and
chapter. one
Where
of
the
efficiency. or the two flow
We
related
that
we have
with
constant
stage
of this this
at
of
For
are other
type
use
only loss, therefore, definition is
stage is
the
in figure exit
kinetic
of equation
(2-68)
into
in the
for
only
correlating parameter
efficiency
correlation,
ease
how static speed
impulse Further
(total energy.
equation
the
(W_:
Assume W2)
stage
diagram assume
efficiency The
efficiency
ratio.
A velocity
2-11.
be
Parameters
blade-jet U_)
the next
is specified,
static
h'o-h'2 Ah' ,7-- h£--h2. ,_ --_h,_ Substitution
in
One parameter must the loading coefficient.
(U_=
is isentropic
to these
speed-work
general
specific the
are
case
case
diagram
(V_._=V_,2).
is shown
turbine
real
Velocity-Diagram
to
axial-flow
be related specific
is required
a more
for an idealized
velocity
can
of velocity
required. is usually to
parameters
idealized general
generally
ratio.
a single
an
more
mathematically axial
efficiency
parameters
Efficiency
show
velocity-diagram
for
type
Lewis
parameters and the
will now
through
addition, shown
a somewhat
speed
of these coefficient,
be
for
In be
a particular
blade-jet
We
will
four
velocity-diagram
Relation
can
these
other.
parameters. section
that
for
that _'=
a
flow
1).
The
efficiency
(2-78) (2-78)
yichts 49
TURBINE
DESIGN
AND
APPLICATION
a1
Vu,1 j/ V2
Wu, 2
FIGURE
2-11.--Velocity-vector
diagram
for
an
axial-flow,
impulse
stage.
UAV,,
(2-79)
= gJAh,.,t The
change
in fluid
tangential
velocity
is (2-80)
zxV,,=V_,,-V_,z From
the
assumptions
convention
(Wl---- W2)
and
(W,._=
and
W,.2)
the
we adopted, (2-81)
W_. 2= --W_. 1 From
sign
equations V,.2=W,.5+
(2-6),
(2-81),
and
(2-80),
U=-W,._+U=-(V,.
we get 1- U) + U=-
V_.I+2U (2-82)
and AV.=V..,I--V.,2=V..1--(--V..,+2U)--2V..I--2U From
the
velocity-diagram
(2-83)
geometry (2-84)
V_, 1= V1 sin m Since
flow
is isentropic
and
the
turbine
stage
is of the
impluse
type
(h2, _d=h_=hl), Vl=_ Substitution 50
of equations
(2-84)
2gJAh_e and
(2-85) (2-85)
into
equation
(2-83)
BASIC
TURBINE
CONCEPTS
yields AVe=2 Substitution
of
sin al_/2gJAhia-2U
equation
(2-86)
back
into
4U sin al
definition
Equation stator only. an
The
(2-88) angle, with
is reached speed
tion
(2-88)
shows
ratio and
that
static
variation
example
0.88 jet
exit
speed
for this and
mathematically
ratio
derivative
of axial-flow,
case
and
of 0.47.
The
by
for of
optimum
bladeequa-
(2-89)
I
I
I
.6
.8
stage.
2-12
to zero:
.4
speed
speed ratio,
ratio Stator
on
ratio
efficiency
differentiating
I
impulse
constant
speed
in figure
.2
blade-jet
any
of blade-jet
sin al 2
Blade-jet
2-12.--Effect
(2-72) (2-88)
equal
Vo_t--
FIGURE
equation
of 70 °. A maximum
speed
the
from
is illustrated
angle
can
setting
ratio
particular
at a blade-jet be found
(2-87)
is a function
is parabolic exit
yields
sin a,--4_3
efficiency
a stator
(2-79)
2gJAh_
of blade-jet n=4z,
equation
4U _
_--4'2gJAh_a Now using the finally yields
(2-86)
static exit
1.0
v
efficiency angle,
of
an
isentropic,
70 °.
51
TURBINE
Since the
DESIGN
the
AND
stator
sine
APPLICATION
exit
of the
angle
angle
is normally
does
not
in the
vary
greatly,
speed ratio for most cases of interest be in the range of 0.4 to 0.5. Equation specific.
(2-88) While
ideal
case,
indeed, very
the
the
figure
2-12
levels
and
values
basic
it does. good
and
We
parabolic find
correlating
Likewise,
for
other
tion
(2-63).
This
does
would
of all sizes.
Such groups.
apply
would
however,
to
apply
be
parameter is found
exit
used
for
or turbine
blade-jet static
would
idealized the
from
same;
speed
and
and
ratio
total
Ds and
parameter
efficiency.
on the variables relating to parameters shown in equathe
number
A parameter not because values of
case,
by
having of the
geometrically not
this
of dimension-
rotative
values
of
at D
similar
having
two
turbospeed
the
all rotative
combining
excludes
the linear remaining
Q
remaining speeds.
of the
is known
\l/2/N2D2\3/4
the
volume
excludes
as
previous
the
specific
NQI/2
flow
rate
is taken
at the
the
Commonly, are 52
quoted
stage
N
(2-91)
is known
as the
specific
diameter
as ( H D_=\-_VD2]
With
N
Thus,
that
is found
is a
parameters.
NE),/2
The
the and,
as
a turbine, exit.
type
will differ
case,
exhaust
found
that
case remain
to a turbomachine
can
very
should both
range in
/
When
of course,
a parameter
because,
parameters N8 and
a
Also,
desirable
The
speed
of this
blade-iet
Parameters
are possible. be desirable
machines variables
not,
that would
variables be
a turbine
of dimensional analysis led to the dimensionless
less parameters dimension D
would
optimum
for a real
for
of 60 ° to 80 °, where
the
velocity-diagram Design
The operation turbomachines
are,
a real
parameter
so are the
with
trend
that
range
volume
but with
flow
not rotative
rate
,,_1/4 (V)
1/2-
taken
at
D,--
DH1/4 Qi/_x
exclusively,
the
speed
N
the
in
DH1/, Q1/2
stage
exit
(2-92) or
turbine
exit, (2-93)
values revolutions
for
these per
parameters minute,
exit
BASIC
volume flow rate H in foot-pounds of units,
Qe_ in cubic per pound,
specific
less because
speed
the
to be the
and
units
are
total-to-total
it is specified Specific
as the
speed
presented
not
diameter
consistent. (5h;_),
total-to-static diagram
parameters.
dimensional
The
ratio
of total
differing eters. all
efficiency
definitions Some
cases, The
thus
eliminating
parameter
speed-work (2-96)
to the
parameter
by
to the
blade
speed
previously
is
or 60 sec/min).
The
(n)-_
(2-95)
and
(2-72)
efficiency
used
use
the can
appears the work
ideal
ratio
from
expressed equation
equations
because
in defining
be
substituting
with
same
efficiency
interrelation
taken
convenience,
(2-94)
(2-93),
work
prefer
for
(27r rad/rev
to static
of ideal
authors
H is usually
be related
The
constant
equations (2-91), (2-95) yields
dimension-
(hh_).
can
H=JAh_d=J_d Combining (2-94) and
head
truly
or head, this set
_ND K
U-where K is the head is
not
sometimes,
value
diameter
are
The but
and specific
velocity
CONCEPTS
feet per second, ideal work, and diameter D in feet. With
specific
value
TURBINE
of the
various
param-
definition
equation in
(2-74)
(2-96).
terms
of
into
equation
NsD8 ' :-- K -v/g_'X -
speed The
and specific exit volume
diameter flow rate
can is
also
be related
to the
Qe_=A_V_ where (2-91),
Since diagram
A_x
is the
(2-93),
specific
flow
area,
(2-94),
and
(2-75)
with
NsD,
3=-- KD2 _'_A_
parameters,
and
specific
which
can
in m 2 or
diameter be used
flow
(2-98)
exit
speed
the
(2-97)
"/l"
Specific coefficient.
in
ft 2. Combining
equation
(2-98)
equations yields
(2-99)
are to
related correlate
to the
velocity-
efficiency,
then 53
TURBINE
DESIGN
specific
AND
speed
and
APPLICATION
specific
diameter
can
also
be
used
to
correlate
efficiency. Specific
speed
and
velocity-diagram flow rate, and (2-99),
diameter
are
sometimes
often
dictate
diameter
that
imply
sometimes referred the
shape. to
type
of design
these for
are
the
equal
applied
thus
overall
following
are
entire
can
that
be
might the
we
have
turbine.
and the
been
When represent
used
some
the
and volume appearing in
speed since
the
specific They
are
shape
will
Parameters
turbine,
the type of design that rapid means for estimating
that
parameters.
parameters,
parameters
and
specific shape
that
or to the
similarity
values to the
The
variables
to be selected.
parameters
to a stage
as
to as design
dimensionless
be applied
Thus,
referred
Overall The
contain
parameters do not. These are diameter their use leads to terms, such as D2/Aex
equation also
specific
most
to a stage,
similar
conditions
efficiency.
parameters
be most appropriate number of required commonly
can
applied
to correlate
of these
discussing
help
and stages.
When identify
serve
encountered
as
a
overall
parameters: Overall
specific
speed __
No1/2
N.----Overall
specific
(2-100)
D"_H1/'
(2-101)
diameter "_
Overall
___e, H3/4
speed-work
parameter (2-102) gj_'_
Overall
blade-jet
speed
ratio
;=
The
subscript
script
(--)
Of nificant
av refers refers
these
overall
considerations erally for that
its on the
specific
contribute
U..
some
value
the
nature speed
to the
value
for
perhaps
determined the
the
super-
evolved
geometry. to show specific
speed.
is most by
other
be restated of overall
and
turbine.
speed
always
Q,_=wv,_ 54
condition,
entire
values
of the can
the
specific
is almost
while
(2-103)
average
for
parameters, value
only,
depend overall
to
to the
because
,
parameters Equation the
sig-
application gen(2-100)
considerations Let (2-104)
BASIC
where
ve_ is specific
flow
rate
volume
be expressed
at exit,
in m3/sec
TURBINE
or ft3/lb.
CONCEPTS
Also,
let
mass
as JP w----_
(2-105)
_'H
Then, (2-100)
substitution yields
of
equations
-_,=1_.7 Thus, three
the
overall
terms.
The
be reasonably
estimated.
gas
thermodynamic
and
the
useful choice
for evaluating is available)
by the
application.
in other
cases,
of N and The
P,
second
both
product
by
in which
as the only
conditions.
the
and
than
of
which
can
on the specified
This
speed
rather
product
performance,
depends
rotative the
equation
oo)
be expressed
term
N_/J__,
into
,=\
expected
cycle
is established
manner
(2-105)
effects that different fluids on the turbine. The third
Often, the
can
reflects
The
the have
vex kll21
speed
term
and
t
/
specific first
(2-104)
second
term
is
(in cases where term is dictated
power
the
are
specified
individual
;
values
application.
overall
specific
speed
influences
the
tur-
axial flow
axial flow One-stage, _'_
A
flow
[
I
I
I
I
I
I
I
I
I
I
.2
.3
.4
.5
.6
.7
.8
.9
1.0
1.1
1.2
I 1.3
Specific speed, Ns, dimensionless
I
I
I
I
I
20
30
40
50
60
I 70
I
I
I
I
I
I
I
I
I
80
90
100
110
120
DO
140
150
160
112)(ibf3/4) Specific speed, Ns, ( ft3/4 )(Ibm314)/(min)(sec t FIGURE
2-13.--Effect
of specific
speed
on turbine-blade
a
shape.
55
TURBINE
DESIGN
AND
bine
passage
shape
bine
and
one-
ratio
for
of hub
speed.
For
decreases
is illustrated and
radius the
APPLICATION
axial-flow,
tip
decreases
to
radius
radius turbines,
ratio.
of the
Dividing
equation
for stage
specific
number (2-100)
speed
for
the
a radial-flow
tur-
turbines.
The
example with
increasing
Thus,
application indicates the type The values of some of the proximation
2-13
two-stage,
axial-flow
the
in figure
increasing
the
overall
specific
or types of design overall parameters
specific
number
of stages
speed
for
any
that will be required. give us a rapid ap-
of stages
required
for
for overall
specific
speed
a given
application.
by equation
(2-91)
yields N_
Qe_
1/2 (2-107)
If we neglect change
per
the
reheat
stage,
effect,
we can
which
is small,
and
assume
equal
H=nH Further,
if the
expansion
compressibility these
effect
last
two
head
write
ratio
and
is not
assume
conditions
(2-108)
into
too
that
large,
we
can
Qe_:-Q_:._t_.
equation
(2-107)
neglect
the
Substitution
and
of
rearrangement
yields n:(NsY/3
(2-109)
\NJ Since
stage
specific
experience assume
can
number
type
overall
speed-work Often,
basis
of stress
suming
2, where
by
requires
value
of blade
equal
Dividing
equation work
Or,
equation
(2-102) blade
per
blade
speed
on
this
can
speed
for
the
for is
is presented.
for
obtained the
of be
the
for
for stage (U2=U_v),
the
overall blade on the
varied
_peed-work
turbine
the
estimate
be selected
may
(2-66) overall
from
value
a value
to
stage
estimate
is often
a knowledge
for
para-
speed-work parameter, and
as-
stage,
ah' =n h' 56
an
an assumed
speed
speed with
known us
correction
of
however,
Thus,
of stages and
Knowledge
efficiency,
specific
speed gives
number
parameter
considerations.
a constant
specific
of compressibility
parameter.
if desired.
of stage
(2-109)
for
for
of efficiency.
a compressibility
speed-work
a reasonable
parameter assuming
effect
parameter,
speed.
overall
of estimate
speed-work
level
equation
The
in reference
metrically
and
parameter
value
a given
assumed
A similar the
a reasonable
requirement, of stages.
discussed
stage
us
is a correlating
to achieve
speed
application
from
tell
in order
specific
speed
(2-110)
BASIC
TURBINE
CONCEPTS
yields n==-
Equations studies
(2-109)
and
associated
(2-111)
with
are particularly
preliminary
Performance The
turbomachinery
perfectly
correct
variables, rate
Q because
considerably Change
for
the
ideal
is the
work
ratio,
depends
we include
number
power work
on the on
as
D
gas #. For
Now,
operating
still R,
simplicity with
heat
ratio
.
some complicated, and speed terms. Let
us operate
we can by using tionality
get
out
but on
of them.
f
not
of the
The
ratio
initial
and to
of
Since
pressure
Since
Mach
temperature
N and
fluid
is
a character-
properties
a molecular heat
H,
express
Ah'.
as on the
variable. speed
specific
T'_,,
are
weight,
ratio
inand
3' is assumed
Ah'
ND
D, R, #)
(2-112)
p,..
w
, -_ ) _/ RT,,,'_T"--7 'P_
been
assumed terms
above
mass-flow
equation,
N,
following:
second-order,
some
the continuity AocD _, so that
the
-- Icn_R-_n'
had
to
variables
produces
-, P; D_
specific
implies the
p'_,, p_,,
w_/RT,.
If the
which
constant.
term
as well
flow
preferred
enthalpy
introduction
here, the
preferred
The
of
Q changes
remains is
in total
Rotative
volume
expansion, w
as another
of interest.
the
pressure
temperature
elasticity.
are
analysis
the
temperature,
w=fcn(_h', dimensional
P,
are
choice
nondimensional to
ratio
on both
temperature
constant
viscosity constant.
while
or drop
initial
of
(2-63)
Another
expressing
pressure
depends
of
to introducing
dimension
turbine,
specific initial
depends
equivalent eluded
flow
Instead
work
for degree
as
parametric
in equation
machines.
w is preferred
significant
expressed
for compressible
actual
presented
rate
for
Parameters
flow
preferred
flow
any
pressure
temperature.
istic
mass
throughout
of
which
is often
The
useful
analyses.
Specification
compressible
however,
performance.
system
parameters for
(2-111)
),
the
(2-113)
constant,
there
modifying
terms parameter ideal-gas
to see
the what
may law,
would
flow,
be
work,
significance
be transformed and
RT .
the
propor-
(2-114) 57
TURBINE
DESIGN
Substitution (2-113)
of this
APPLICATION
relation
into
the
mass
flow
parameter
of equation
yields
Thus,
the
mass
of actual the
AND
critical, The
flow
mass speed
flow
rate rate
is represented to the
or sonic,
velocity.
parameter
may
nondimensionally
mass
flow rate
when
be transformed
by
the
the
velocity
ratio equals
as
ND
U U oc ,-7-_,_, oc-_]RT't,, _RT,_ ac, Thus,
the
rotative
of rotor-blade Mach
speed
velocity
number.
parameter fluid
have
certain
with
V/U,
Mach
number,
as for
temperature
a given
(2-113)
with
can
in order
be
the
for
rotor
critical the flow,
the
effect
only
velocity.
For speed
becomes
of varying
speed
be inlet
presented
The
must
also
must
parameters
of rotor the
must
but
ratio
similarity.
rotative
All variables
dimensionless
expressed
not
to the
fluid.
by
of
the
the
is a kind
parameter
condition but
incompressible
by
similarity,
therefore,
of the
gas,
for
respect
dimensions,
dimensionless form to be correlated. For
kinematic
a certain velocity
which
mass-flow
is that
variable the
the
nondimensionally velocity,
the
analysis
of fixed
singular
of
of this
fixed
machine
to critical
Division
gives
implication
is represented
(2-116)
the
have
a
a given is not
a
associated expressed
in
temperature as equation
as
(2-117) p_---_
For
a given
gas
-_-Icn
in a given
_T-'
turbine,
_=fcn
Depending tions
on
the
(2-113),
particular
(2-117),
or
the
_-r,
case,
--7'
the
(2-118)
parameters
further
be
to
(2-118)
-r-,
parameters
can
reduce
presented
used
to
in equa-
express
turbine
performance. Equivalent It
is very
useful
of temperature and 58
specific
to report
and heat
pressure
ratio.
This
Conditions
performance and
under
sometimes
is done
in order
standard
of fluid that
conditions
molecular results
weight
obtained
at
BASIC
different easily
conditions used
following sure,
may
are
101
the
325
as
of these Let constant.
With
subscript can then
are
parameters
the
known
with
basis
diameter
conditions similarity
and
the
conditions
(2-119)
!
Ah'eq l_,d
N
(2-120)
N_q
/
these
The
the
Pst_
ah' RT_.--R_,.
of
air. on
but
the
or are
conditions.
standard
P
P_.
Rearrangement conditions
standard
expressed
(2-113)
conditions,
K
1.4. These
as equivalent
std denoting
equivalent as
pres-
288.2
ratio,
NACA
speed
also The
atmospheric
heat
or and
and
we desire.
temperature,
of equation
subscript
eq denoting be expressed
used:
specific
work,
CONCEPTS
compared
condition
psia;
and
conditions,
of flow,
conditions
the
readily
usually
14.696 29.0;
standard
variables
us use
or
weight,
standard
and
for any
conditions
N/m _ abs
NACA
performance
directly
performance
standard
518.7 ° R; molecular known
be
to determine
TURBINE
,
(2-121)
equations
then
yields
for
the
equivalent
p',. w,q.=w
taT' ta
,
Ah_q-----,_h
(2-122)
, RT',_
(2-123)
N_q= N 4R--_ta / T:,a ,
by
As you may recall, assuming constant
always and
the
case,
fluid.
Let
since
The
used
yield
do not
(sonic)
velocity.
specific
heat
and
have
specific add
similarity and
a very
commonly used are expressed as
heat
ratio
change
corrections
under the
Mach small
can
a specific-heat-ratio
specific-heat-ratio However,
ratio
only
we started off the discussion of these specific heat ratio for all conditions.
us now
parameters.
(2-124)
all
terms number,
effect
specific-heat-ratio
conditions, that are
are
the
temperature
effect
into
the
that
are
commonly
but
only
out
depend
cumbersome
on equivalent terms,
left
with
parameters This is not
at
critical on both
to work
conditions. equivalent
above
with,
With
the
conditions
59
TURBINE
DESIGN
AND
APPLICATION
(2-125)
V_.v_,,.J \p,.:
8q--
----
t
(2-126)
_:,=t,h' ,,,_7 ) N_q_
Nj(V_'d.)
'
(2-127)
where
.>,,S. _2 V,;(,,,:,) "\%,,+1/
(2-128)
.d__Ly<.,-,,
_-
'\,y+ 1/ and,
as you
recall, 2 27 V<,--_-_l
Therefore, 127)
for
reduce
constant
specific
to equations
Finally,
heat
(2-122)
(2-129)
gRT' ratio,
equations
(2-125)
to
(2-
to (2-124).
we define 0=(
Vc, kYcr.
)2
(2-130)
8ldl
and #
.--_--P-_",
(2-131)
Pstd
The
equivalent
conditions
are
then
expressed
w,q=w
_
as
_
_kh
(2-132)
#
0
_'_--
(2-133)
N Neq=_ One
point
operation of both reduce effect
that
can
be seen
at temperatures actual the
mass
output
is the reduction
greater
flow of
and
The
6O
be
effect one
in takeoff
of viscosity of
the
these than
in the
dimensionless
similarity
standard
equivalent
equations will cause
speed.
a powerplant.
Reynolds
to
from
(2-134)
Both
A well-known
performance Number form
of jet
a reduction
of these example
aircraft
on hot
factors of this days.
Effect
of Reynolds
parameters
is that
number
affecting
was
shown
turbomachine
BASIC
performance.
While
its
effect
effect of Reynolds number the following manner: Expressing
efficiency
it is still
efficiency
CONCEPTS
important.
is usually
The
correlated
in
as 7'
we can
is secondary,
on turbine
TURBINE
A '
'
hh'_
Ah' 5h'
(2-135)
ld
write _h
,
,
• -7 If we assume
that
the
only
loss
J
,o,
=
(2-136)
is friction
loss,
(2-137)
where length.
f
is the friction factor, For turbulent flow,
and
L is the
characteristic
flow-path
1 fOCR--_0._ where and
Re
is the
Reynolds
number.
into
equation
(2-136)
(2-137)
1--_'
Adding
subscripts
dividing yield
Since
the
for
equation
for geometric
V_/Ah_.,_-=V22/Ah
This the
range
all
the
attributable another
is an for
1 and
(2-140)
correlation. type
of 0.1 to 0.2, losses
are
not
to viscous suggested
type
the
(2-139) for
reduces
depending
on the losses,
mmilarity
varies
of correlation
(2-141)
0.2,
machine. and
between
2
to
it has
is not
and
condition
and for dynamic
Actually,
viscous
equation
equation
(Re_'_ °'2 \Re1/
of correlation
loss
2 to
1 by
L_/DI--:L_/D2
'_,_d, equation
this
(2-138)
(2-139)
condition
similarity
ideal
equations
1
1--7; 1--72
exponent
Substituting yields
conditions for
(2-138)
the
been but
found
This
of In
the
varies
occurs
fraction
machines.
that
usually
in
because total
view
loss
of this,
is 61
TURBINE
DESIGN
AND
APPLICATION
1--v_--A
where the
A and
exponent
B are
such
is maintained
and
the
loss
is viscous
coefficients
discussion
fractions
loss.
A
to 0.4 for A and
be
a good
that
and in
to represent
turbine
tests
for
here
viscous the
values
correlating
fact
that
of 0.7
Reynolds
(2-142)
loss
at Lewis,
1, indicate
corresponding
compromise
1. In equation the
B serve
reference
(2-142)
A+B=
at 0.2 to reflect
Recent
presented
0.3
{Re2"_ °_
exponent,
that
not
as well
values
of
to 0.6 for number
all
as the about
B seem effects.
REFERENCES 1.
SHEPHERD,
D.
2.
GLASSMAN,
ARTHUR
eters Ratio
62
for
G.:
Principles J.;
Examination
Axial-Flow
of
AND
of Turbines.
Turbomachincry.
STED/ART,
WARNER
Geometry NASA
Macmillan L.:
Use
Characteristics TN
D-4248,
of of
1967.
Co., Similarity
1956. Param-
tligh-Expansion-
to
BASIC
TURBINE
CONCEPTS
SYMBOLS A
flow area, Reynolds
a
speed
B
Reynolds
C_
heat
D
diameter,
D_ E
specific
e
kinetic
F
force, N ; lb friction factor
]
m2; ft 2 number correlation
of sound,
m/sec;
number
capacity
(2-142)
coefficient
in eq.
(2-142)
pressure,
J/(kg)(K);
dimensionless;
of elasticity, energy
N/m2;
loss
(sec I/2) (lbfl/4) / (ft I/4) (lbm 1/4) lb/ft 2
coefficient,
constant,
defined
g H
conversion
h J
specific enthalpy, J/kg; Btu/lb conversion constant, 1; 778 (ft)(lb)/Btu
K
conversion
L M
characteristic Mach number
N
rotative
N,
specific
?%
number polytropic
P
power,
P
absolute
Q
volume
R
gas constant, reaction
Re
Reynolds
r
radius,
T
absolute
U
blade
head,
J/kg;
constant,
eq.
(2-46)
(Ibm)(ft)/(lbf)(sec
2_r rad/rev;
length,
speed,
2)
60 sec/min
m; ft
rad/sec;
speed,
rev/min
dimensionless;
(ft 3/4) (lbm 3/4)/ (rain)
(sec 1/_) (lbf 3/4)
of stages exponent W;
Btu/sec
pressure, flow
rate,
N/m2;
lb/ft 2
m3/sec;
ft3/sec
J/(kg)
(K) ; (ft) (lbf)/(lbm)
(°R)
number m; ft temperature,
speed,
velocity,
Vj
ideal
V
specific
volume,
W
relative
velocity,
20
mass
jet speed
flow
K;
m/sec;
absolute
rate,
!:1
total-pressure fluid
1 ; 32.17
by
(ft) (lbf)/lbm
V
OL
Btu/(lb)(°R)
ft
diameter,
modulus
in eq.
ft/sec
correlation
at constant
m;
coefficient
absolute
deg fluid relative
°R
ft/sec m/sec;
(defined
by
mZ/kg;
loss
(2-71)),
m/sec;
ft/sec
ft/sec lb/sec
coefficient,
angle angle
eq.
ft3/lb
m/sec; kg/sec;
ft/sec
defined
by
eqs.
(2-47)
measured
from
axial
or radial
direction,
measured
from
axial
or radial
direction,
deg 63
TURBINE
DESIGN
ratio
7
AND
of heat
constant ratio
APPLICATION
capacity
at constant
pressure
to heat
capacity
at
volume
of inlet
function
total
pressure
of specific
heat
to NACA ratio,
standard
defined
by
eq.
pressure (2-128)
efficiency 0
squared
ratio
perature
of critical to
velocity
critical
based
velocity
on
based
on
temperature speed-work viscosity, y
blade-jet
p
density,
T
torque, flow
¢
parameter, (N)(sec)/m_; speed
ratio,
kg/mS; N-m;
defined by lb/(ft) (sec) defined
defined
coefficient,
angular
velocity,
by
defined rad/sec
Subscripts: av cr
average critical
eq ex
equivalent exit
/d
ideal
in
inlet
loss
loss
opt
optimum
p
polytropic
r rel
radial component relative
ro
rotor
st
stator
std
NACA
stg u
stage tangential
x 0 1
axial component at stator inlet at stator exit or rotor
2
at rotor
condition
(M---- 1)
standard
condition
component
exit
Superscripts:
'
absolute
"
relative
64
(2-72)
lb/ft a
coefficient,
vector overall
eq.
(2-66)
lb-ft
loading
--_ --
by
eq.
quantity turbine total total
state state
inlet
eq. (2-75) by
eq.
(2-67)
turbine NACA
inlet
tem-
standard
BASIC
TURBINE
CONCEPTS
GLOSSARY The
terms
defined
herein
are
illustrated
in figure
2-14.
Tip-___
FLow_
I Blad_
_Hu b
I/-Suction
surface
Leading edge-/" Pressure surface J/
Camber line-_ /-Trailing
edge
Axis-/ /
_ Opening, or th roat
/ /
Tangent to camber / line at leading edge 4.
Chord
\ \
l Spacing. or pitch
Blade inlet angle 7 \...\ /
Axis-,,
/
Flow inlet angle-/ FIo_ / I
Incidence angle J /
/_-Tangent to camber line at trailing edge Flow exit angle
Axial chord Deviation ant
FIOURF
2-14.--Blade
-Blade exit angle
terminology.
65
TURBINE
DESIGN
aspect
ratio.
axial
chord.
AND
The
ratio
The
length
turbine, onto of the blade. axial
solidity.
blade
exit
at the
The
height. inlet
parallel
The
angle
The
and
radius
angle.
tangents equal
The
to the to the
chord.
The
line
of the
at the
length
the
chord
between chord line. up on where
axial
length
to the
camber
line
direction. the
radius
at the
tangent
by
the
leading
formed
to the
hub. camber
line
direction.
formed
angles
in the
spacing.
tangent
axial
mean
line
of the
intersection
and by
blade
edge to the trailing edge, and the suction surface.
The
onto
camber
to the
the
turbine
as set
axis. It is the
tip minus
angle
blade,
axial
between
external
chord.
of the
trailing
the
of the
edges.
chord
line
It
is
and
the
from
the
tangents.
line.
leading surface
the
turbine
and the blade.
sum
camber-line camber
between
angle
at the leading edge bucket. Same as rotor camber
chord
the
to the
turbine
axial
at the
The
height
projection to the
of the
edge
angle.
blade
of the
ratio
angle.
blade
of the
a line
trailing
blade
APPLICATION
of the line.
profile.
halfway
perpendicular
a flat surface, the front and
extends
between
projection
It is approximately
the leading edge and If a two-dimensional
It
equal
of the to the
the trailing edge. blade section were
the chord line the rear of the
is the blade
the
pressure
blade
linear laid
profile distance
convex
line between section would
side
the points touch the
surface.
deflection.
The
ference
total
between
deviation
the
angle.
The
flow exit angle. exit and the
The
hub-tip hubleading mean nozzle
section. blade.
pitch.
The
points
66
The The
ratio.
and
ratio
inlet
in the
adjacent are
flow
the
blade
flow
angle.
exit
direction flow
dif-
angle. at the
direction
blade at
the
ratio.
of the
minus
of the
direction
hub
radius
to the
the
blade
between
the
inlet
tip radius. angle.
blade.
of rotatioll
hub
between
and the
tip.
corresponding
blades.
The
concave
surface
of the
highest.
Same
exit
to the
blade.
angle
or nose,
It is equal
the
fluid
to tip-radius
The
flow
front,
fluid.
minus
The blade section halfway Same as stator blade.
surface.
pressures radius
angle
angle
of the
as hubratio.
distance on
pressure
of the
between the fluid axial direction.
section
Same
angle. edge.
inlet exit
The angle the turbine
to tip-radius
incidence
flow flow
innermost ratio.
angle
The angle between the turbine axial direction.
flow inlet angle. blade inlet and hub.
turning
as hub-
to tip-radius
ratio.
blade.
Along
this
surface,
BASIC
root.
Same
rotor
blade. The
spacing.
Same
A rotating
stagger angle. direction. stator
tip.
blade.
ratio
blade.
of the
chord
angle
between
A stationary
surface.
edge.
to the
spacing.
as pitch. The
The
The
rear,
the
chord
line
and
the
turbine
axial
blade.
convex
pressures are lowest. The outermost section
trailing
CONCEPTS
as hub.
solidity.
suction
TURBINE
surface of the
or tail,
of the
blade.
Along
this
surface,
blade.
of the
blade.
67
CHAPTER 3
Velocity Diagrams By Warren J. Whitneyand WarnerL.Stewart As
indicated
in chapter
be considered the
fluid
in the
velocities
universally overall
design
these
blading
next
cussed
the
to the
in chapter velocity
efficiency
is devoted
entirely
part
of this
Usually, second
the part
diagrams and
chapter
representative
from
turbines
of this
that the are
variation considered
rotative
expected
of the
also
concerns at
illustrated
blade
balance
blade
in this
speed
conditions
mean to the of forces with
that
radius radial in the radius.
the
diagrams turbine.
turbine
and
were
dis-
associated
with
2,
and
their
case.
This
an idealized
diagram
flow
in
diagrams
chapter
of velocity
a single
is devoted the
by
subject
average the
in
are
important
the
parameters
presented
are the
diagrams.
velocity
from
capacity
row Once
velocities
the
flow
was
in
and
of and
speed
velocity is very
angles
level
to the
from
and
addition,
dimensionless
chapter
result
work,
of the
velocity
blade
diagrams.
geometry
flow In
of the
and
of the
conditions
speed
to
absolute
of velocity
velocity
were
to turbine
The
constructing
2. Various
diagram
is the
next.
for
work
chapter sidered
the
efficiency
relation first
blading
variables
of turbines
evolution
produce.
methods
them
flow,
is the
specify to
affect
general
of
use
important
to the
to the
the
required
diagrams
most
row
relation
step
to the
significantly relating
their
blade
through
is required
The
one
requirements the
relation
that
the
and
of the
or analysis
from
described
established, Their
design
as it passes
relative
2, one
diagrams. that
can for
are
The be
the used.
variations
constage. The
in the
radial
direction
Only
axial-flow
chapter. 69
TURBINE
DESIGN
AND
APPLICATION
MEAN-SECTION In
this
section,
(halfway
the
between
conditions grams,
hub
review, the
clature.
to 3-1
vector
are
the
assumed
turbine.
stage
at the
mean
section
the
average
to represent
The
efficiency,
shows
no
(2-14)
an
relations
Assuming
equation
tip)
occurring
different
and
of dia-
selection
when
their
types
are discussed.
figure
indicating
diagrams
by
relation
is required
In
and
encountered their
staging
velocity
DIAGRAMS
illustrative
described in
be written
as
can
change
stage
velocity
in chapter
mean
2 and
radius
diagram the
through
nomen-
the
stage,
ah ' =--UA V_' gj
(3-1)
where h'
total
enthalpy, speed,
J/kg;
Btu/lb
U
blade
V,
tangential
component
m/see;
g
conversion
constant,
1 ; 32.17
J
conversion
constant,
1 ; 778
relates
ft/sec of velocity,
This
equation
the
The
axial
component
of
rate,
state
conditions,
and
m/see;
(lbm)
(ft)/(lbf)
specific
work
velocity
the
(sec 2)
(ft) (lb)/Btu
stage the
ftlsec
area
to the
vector
by
the
velocity
is related
diagram. to
the
flow
relation
_0 Vz
=
(3-2)
P-_an
where Vx
axial
component
w
mass
flow
o Aan
density, annulus
Flow only
are
the
axial
the
absolute
also
affect
kg/see;
key
the studies
because
shape.
Such
such
are
to
and
in
parameter
parameter,
7O
the
swirl
velocity)
geometry. can
discussed can
they
not
component
association
which
be
but
In addition, with
in
of
velocity-
related chapter
be expressed
to the 2 and
in several
as U2 U _=gJAh'--AV,,--
The
as
values
were
because
tangential
blading
used
parameters
speed-work
(the
referred
efficiency the
parameters
velocities
is often
parameters
diagram ways,
swirl
expected
diagram
the
ft/sec
velocity-diagram
and
velocity
dimensionless
include
m/see;
lb/sec
kg/m3; lb/ft 3 area, mS; ft 2
angles
link
of velocity,
rate,
speed-work
parameter
is used
in
g JAb' AV_ 2 this
chapter
(3-3) because
diagram
VELOCITY
DIAORAMS
FI0w
VX,0 Station 0
Vx,
VI
al-'"
i" i'll
,,
I
w z v/Ivu, Vx, 2
../
u
!
_/Vu .2
I
WU,2 3-1.--Velocity-vector
FIGURE
types
are
related
normalize
the
to
the
diagram
diagrams
swirl
and nomenclature.
distribution
velocities
by
and
Velocity-Diagram After
the
diagrams
can
shapes
design on the
Diagram
exit
(V_._) and diagrams in this
type
refers
the
rotor their
the and
exit
(V_._).
reaction
Zero-exit-swirl
diagram
(V_._---- 0)
(2)
Rotor-impulse
diagram
(W, = W2)
(3)
Symmetrical
diagram
three diagrams in figure 3-2.
Zero-exit-swirl velocity efficiency.
head The
for
(V_--W2 several
diagram.--In or
the
swirl
zero-exit-swirl
value
reaction
(1)
These shown
the
to
values many
component diagram,
Vu., _ 1 hVu--
of the
values
swirl
and
V2:W1)
either
and
speed-work imposed between
three
the
common
characteristics
of speed-work
thereof
sizes
of performancesplit
following
and
cases,
velocity
constraint
swirl
The
the
different
physical
determines
as stage
and section:
established, have
and
to some
shape
such
are
diagrams
diagram
type
parameters,
types of discussed
Velocity
is convenient
Types
requirements
evolved.
Diagram
diagram.
related stator
be
depending
parameter. on the
overall
it
AV,.
are
parameter the
represents
are
entire
exit
a loss
in
where
(3-4a)
and 71
TURBINE
DESIGN
AND
APPLICATION
Speedwork
Diagram type
parameter
Zero exit swirl
Impulse
Symmetrical
O.25
0.5
1.O
FIGURE
3-2.--Effects
of
speed-work stage
parameter
be
used
For
an
to reduce axial-flow
(Vz.1=Vz.2), (2-39)
such
the
reduces
diagram
type
on
shape
of
diagram.
V_.2_ AV,-can
and
velocity-vector
0 (3--4b)
loss.
rotor
(UI=
definition
U2)
of
to
W2 R.,--
having
stage
constant
reaction
axial
presented
in
velocity equation
W2 u, 1 2+W ,2-W .t
(3-5)
_, 2--
1-
where Rst_
stage
W_
tangential
By
using
(3-5)
reaction component
equation
can
be
(2-6)
expressed
of relative and
equations
0.5, is
equation which
zero,
reaction --0.5, velocity 72
is plotted
indicates which
and
indicates as can increase
and
ft/sec
(3-4),
equation
1 1--_-_
in
figure
a conservative an
is encountered. which,
(3-3)
m/sec;
as Rs,g=
This
velocity,
be
shown,
in static
3-3(a).
At
diagram.
impulse
For
(3-6)
represents pressure
At
rotor.
example,
at
_---1,
the
k=0.5,
Below
the
_=0.5,
_,----0.33,
the
a substantial across
the
reaction
rotor.
is
reaction negative
reaction
is
decrease
in
Because
of
VELOCITY
DIAGRAMS
1.0--
Symmetrical_ \
.o_
ZeroS,
_- Impulse
(a)
I
/
I
1
I
.5-::3
N
Zero exit swirl-, 0
,m
(b)
I 0
I
.25
I
1
.50 .75 Speed-workparameter, _,
1.0
(a) (b) FIGURE 3-3.--Effects
potentially avoided;
high Figure
losses,
Impulse
such
presents
negative
reduces
and
are
zero-exit-swirl negative-reaction
this
case,
WI=W2
axial
equation velocity,
(2-6), the
rotor
are
type
usually
seldom
used
for
diagrams
for
the
cases. and
the
equation
for
to Rst_=O
From
diagram
reactions
diagrams the
impulse,
diagram.--For
reaction
high
zero-exit-swirl
3-2
positive-reaction, stage
Reaction. Exit swirl.
of speed-work parameter and velocity-vector on reaction and exit swirl.
therefore,
X<0.5.
.
equation inlet
(3-3), and
exit
(3-7) and swirl
the
assumption
velocities
can
of constant be expressed 73
TURBINE
DESIGN
AND
APPLICATION
as
V_, _ AVu--
X+0.5
(3-8a)
_,--0.5
(3-8b)
and Vu
_-_= The
exit
swirls
swirl
are
characteristics
encountered
at
swirls are obtained and zero-exit-swirl figure
3-2.
positive
seldom,
if ever,
Symmetrical one
in
specified
_ values
swirl swirl
used
when
the
to have
the
same
0.5,
Positive
and
negative
leaving
is
a
turbine
work, than
type and
shape.
than
3-3(b).
the impulse illustrated in
_ is greater third
figure
than 0.5. At _=0.5, These effects are
stage
stator-exit-
in
greater
velocity
decreases
diagram.--A
which
shown
at _ values less cases coincide.
Because
because
are
impulse
and are
0.5.
of diagram
commonly
rotor-exit-velocity
In terms
a loss
diagrams used
is
triangles
are
of velocities,
V1 =W2
(3-9a)
V2=W,
(3-9b)
and
Under
this
condition,
the
equation
for stage
reaction
reduces
to
1 R,tg=_ From
equation
axial
(2-6),
velocity,
the
equation
swirl
(3-10)
(3-3),
velocity
and
the
components
Vu. 1 AV_
assumption can
of constant
be expressed
as
X+ 1 2
(3-11 a)
and Vu. 2 h_l A-V_= 2-These
reaction
typical is the
same
decreases, at 0.5. this (e.g.,
and
diagrams as the the This
type the
swirl
swirl
of diagram and
attractive middle
74
aspect
but
is conducive
The at
the
of a turbine
in figure
symmetrical _=
1. As
reaction
to high
for stages stages
Stage A significant
3-2.
diagram
increases,
reaction
are shown
in figure
zero-exit-swirl
exit
good
front
characteristics
illustrated
(3-11b)
where
the
value
swirl
of
constant
efficiency,
exit
of a multistage
with
diagram
remains
total
3-3,
making
is not
a loss
turbine).
Efficiency design
is the
expected
efficiency.
VELOCITY
The
efficiency
type blade on
is an
important
of velocity diagram surface. Therefore, the
efficiency
basic
relations
sented
and
effects.
References
function
between
in
of
diagram
herein
to
1 and
As presented written as
among
used and the pressure the diagram selection
requirements
used
of,
the
2 are
chapter
2,
up
of
used
as a basis
turbine
stage
the
on the dependent
application.
and
some
things,
distribution is greatly
intended
parameters
point
other
DIAGRAMS
efficiency
are
more
important
the for
Some
this
static
pre-
development.
efficiency
can
be
hh' _--Ah_d
(3-12)
where stage
static
efficiency
Ah'
stage
work,
J/kg;
Btu/lb
hh_
stage
ideal
work
based
static Expressing
pressure, ideal
on
J/kg;
work
ratio
of inlet
total
pressure
to exit
Btu/lb
in terms
of actual
work
plus
losses
yields
ah' ,hh' +Lot'-b
Lro+
V22
(3-13)
where Lst
stator
Lro
rotor
loss,
y /2gJ
stage
leaving
The
equation
nation into
of the equation
loss,
for
J/kg;
Btu/lb
J/kg;
Btu/lb
loss,
total
stage
J/kg;
efficiency
leaving
(3-13)
it
was
kinetic
relating
the
assumed energy
stator that
across
n' is the
loss,
V]/2gJ.
same
except
for
Substituting
the
equation
elimi(3-3)
yields
,1--
In
Btu/lb
gJ(L,,TLro)
and the
the
rotor losses
blade
losses were
rows.
L,,:K_,
1
V2 2
to the proportional
That
(3-14)
diagram to
parameters, the
average
is,
V°2-b V_2 2gJ
(3-15a)
and L_o=K_o
where/4
is constant
Wl2+W2_ 2gJ
(3-15b)
of proportionality. 75
TURBINE
DESIGN
Equations
AND
(3-14)
efficiency.
The
and
exact
in references
efficiency
is as follows:
(1)
velocities
The
(3-15)
nature
be found
axial
APPLICATION
of
1 and are
serve the
(2) The
tangential
(2-6)
expressed
related
according
and
(3) The
the
in
eq.
axial
(3-4),
the
(3-8),
components
mass-flow
are
to
or
are
for
and
of
estimating
equations
procedure
terms
for
their
assumption
or
can
estimating
tangential
and
by
an angle
assumption.
values
for
constant
basis (5)
of previous
Efficiency
work
parameter
The
total-
erence
2 by
presented that
for
various
determined
the
the
reaction
The For
total
each
efficiency
parameter, higher
},, value than
the
efficiency _-_0.5, other the
at two
for
efficiency
decreases High rather
swirls
this
chapter,
The
static
symmetrical
ref-
curves diagram
diagram,
as
diagram,
and
of those
curves for the zero-exit-swirl less than 0.5 because of the
for
diagram undesirable
region. the
are
highest
presented
efficiency
in figure
occurs
s)_nmetrical-diagram
equal
is equal to
not
the
shown, less
are rather
than fiat.
at
for
all
to the
0.5.
is slightly
values
of
_. The
symmetrical-diagram
impulse-diagram becomes
3-4(a).
a speed-work
efficiency
efficiency
less
efficiency than
Between
either
_1
As h is reduced
still
are
greater
than
consider
the
is the aspects
three-dimensional
before
a diagram
efficiency exit
therefore,
efficiency
efficiency" the
the
This
representative
_ values
static, and
static
because
for
must
exit
for
efficiency. the
efficiencies,
types
designer
actually
The
and
below
0.5,
at
of the },_0.5, efficiency
rapidly.
total than
from
3-4.
are
}, values
curves
more
diagram
is
on
of speed-
as obtained
characteristics
efficiency
although
selected
a range
in figure
are
total
impulse-diagram
}_--1,
and,
tangential
are
over
presented
diagram
of 1. The
zero-exit-swirl-diagram
the
types.
characteristics
type,
to
2, approximates
in that
diagram
speed-
considered
of an application-
them
characteristics are
a symmetrical diagram. The were not obtained for )_ values negative
relating
diagram
maximum
efficiency
means
be generated
symmetrical
in reference
associated
then
method
)4elds
by
of proportionality
static-efficiency above
of the
being
experience. can
and the for
test
curves
analytically
the
the
in terms type
(3-11)). by
(4)
The
expressed diagram
evaluated
components
76
basis
assumptions
2. Briefly,
components
parameter
(eq.
The
the
components.
work
the
as
type
is substantially head
about
criterion such
with
0.5. of
as the
effects,
characteristics
velocity
achievable
any
Even
of these
where
merit,
total,
however,
the
previously
discussed
to be discussed
later
is selected. are
presented
lower
than
represents
a loss.
in figure the The
total
3-4(b). efficiency
highest
static
in
VELOCITY
efficiency diagram, diagram. _=0.5,
for
h values
less
than
0.5
and
for
X values
greater
For
the
impulse
diagram,
where
there
is no
is
obtained
than
exit
0.5,
the
swirl.
with
with
efficiency
For
the
DIAGRAMS
the
the
impulse
zero-exit-swirl
is a maximum
symmetrical
at
diagram,
1.0
.8
f,,_.._=--_'---u-
.6 e-
-% _6
Diagram type
.4
Zero exit swirl Impulse Symmetrical .2
(a)
I
/
/
I
///
I
I
I
/ /
// /
I
(b) 0
.2
.4
Speed-work parameter,
FIGURE
3-4.--Effects
(a)
Total
efficiency.
(b)
Static
efficiency.
of speed-work on
efficiency.
I .8
.6
parameter (Curves
and from
I 1.0
;_
velocity-vector ref.
diagram
type
2.)
77
TURBINE
DESIGN
AND
APPLICATION
.90 -Total efficiency, 7'
.80-t--
L_
• 70
iency, "q
6O
1
I
I
J
65
70
75
8O
Stator exit angle, % deg 3-5.--Effect
FIGURE
of stator exit eter X, 0.5.
the
efficiency
The
zero-exit-swirl-diagram
very
little
is a maximum
which
type
but
obtained shows
from the
and
that
maximized.
If
should
stator
exit
of
angle of
through-flow
stress
influence
It
has
large
been
exit
are
One
means
use
of downstream
back
to axial. presented
stream shows 78
the
total
which
total
efficiency
does
swirl.
decreases
not
parameter component
of this
is taken
from
upon
which
is
desired,
and,
by the
exit
the
is to be
stator
complete
exit
affects
the
annulus
area
a
freedom
it
the
annulus
1,
angle.
is desired,
since
therefore,
be
reference
efficiency exist
can
efficiency
However,
always
V=,
effect
of stator
static
and
area.
and,
hence,
selection.
that
at
low
values with
of increasing
stators,
are
example
depends
encountered,
The
param-
exit
at _ = 1, but
as functions
is also influenced
which
efficiency
in figure
staters that
3-5,
of velocity
shown
no
speed-work
75 ° is indicated.
angle
swirls
efficiency.
are
level
is
through-flow
An
angle
angle
the
velocity
angles.
60 °. If maximum
of about this
the
efficiencies
best
about
there
is highest by
1. Figure
component
rotor
could
the
flow
static
the
only
by
maximum
be
selection
The
also
reference
It is evident angle
not
to the
total
where
Speed-work
to 0.5.
is affected
is related
X= 1,
at
efficiency
as _, is reduced
Efficiency diagram
angle on stage efficiency. (Curves from ref. I.)
3-6.
referred
of
associated
the remove
static the
characteristics In
this
to
as
efficiencies
of
speed-work
1X-stage
the
diffuse
flow
(ref.
with Figure
turbines
the
the
turbines
turbines
turbines.
l_-stage
in static
is through
and
of such
figure, the
reductions
efficienc:_ swirl
parameter,
3)
down3-6(a)
are
lower
VELOCITY
than
those
are
due
Because no
gain
of the
1-stage
turbines.
to the
additional
friction
of this
additional
friction
in static
efficiency
value
of X is below
below
about
through
impulse
0.35,
use
over
losses loss, that
approximately substantial
lower
of the
total
efficiencies
downstream
stators.
the
l_-stage
of the
1-stage
0.35
gains
of downstream
These
(fig.
in static
DIAGRAMS
turbine turbine
3-6(b)).
For
efficiency
can
achieves until
the
X values
be achieved
stators.
1. O0
Diagram type
impulse
1-Stage ll-St_e
impulse
ll-Stage
symmetrical
l_-Stage
impulse (two
downstream
o
I
I
stators}
I
I
.60
¢.-
.40
0
FmuR_;
3-6.--Effect
.i
of
.2
.3
Speed-work
parameter,
(a)
Total
(b)
Static
downstream
.4
.5
h
efficiency. efficiency. stator
on
efficiency.
(Curves
from
ref.
3.)
79
TURBINE
DESIGN
AND
APPLICATION
Multistage
Turbine
Efficiency
When the turbine requirements are such that the speed-work parameter is quite low and high efficiencies are still desired, multistage turbines are used, and the required work is split amongst the various stages.
t-
stages Turbine
o_ ro
2 2
ta_
.!
/
7° I
o--
_ N
I
I
I
1
I
.f/..i
/ ,/,/"
50
//,,," /,
•40
tb) 0
FIGURE 3-7.--Comparison
8O
I • 10
1
I
.20 .30 Overall speed-work parameter,
] .ZlO
(a) Total efficiency• (b) Static efficiency. of efficiencies of 1-, l_/r -, and 2-stage from ref. 4.)
I .50
turbines.
(Curves
VELOCITY
Two-stage turbine the
$urbines.--The
results
in about
reduction
stage
addition
of
doubling
stage
work.
_, is accompanied
with
two
the
stages
exit
swirls
A study sented (from
4. The
4)
are
total the
the
2- and
efficiency
1-stage 1-stage and
difference
between
than
for
24
the
total
1-stage
The
2-stage
turbine
work
good
symmetrical
maintained by
increased
the
first
stages
diagram
The
as well
is illustrated
in figure
velocity
compounded. (or
increase)
Figure
3-8(b)
two-stage stator. exit
with
The swirl
second-stage
diagram and
characteristics ciencies obtained
the
with
of this
positive
the
exit
3-7
speeds
with
swirl
of turbine
upon
the
and
no
50:50
each
stage.
exit
swirl
of the
work
work impulse
split
has
first
and
This
a type
in which
type
of
of turbine
all expansion
stator
and
and
the
equal. was
for without
another
subse-
first-stage type
X=0.125
case of the
with
in reference
the
first
zero
efficiency 5. Effi-
two-stage turbines blade row. Because
leaving
of
a second-stage
A study made
all
in velocity. condition is
decreasing
diagram
swirl
the swirl
a
zero
stator.
first
swirl
for
are exit
with for
the
a velocity-compounded
turbine
is again
blade
for
output.
and
exit
represents
the
velocity
turbine
work
split
total
smaller
loss
fraction
turbine in
counterrotating
depends
The
optimum
general,
for
2-stage
total
features
higher than those for conventional because of the elimination of one work
points
the flow with no change the velocity-compounded
the
type
between
diagrams
and
In
increasing
shown
efficiency
figure
second-stage
is achieved
both
static difference
is maximized
three-stage)
illustrates
turbine,
of no
3-8 (a)
quent blade rows merely turn As k is reduced below 0.125, maintained, but work fraction.
work
diagram
impulse
is a two-stage velocity
in
stage
an increasing
associated
as
(fluid
presented
_=0.125,
turbines
speed-work
leaving
is achieved
and
At
turbine
and
is pre-
2-stage
the
of the
efficiency
kno_:a
split
turbines
overall
the
the
fraction
efficiency
as an
in
addition,
work
efficiency.
because
criteria
stage
stage.
increase
a 2-percentage-point-
for
zero-exit-swirl
second
to 75:25.
second
an
static
varying
_=0.5,
maximum
in the
produced
smaller
diagram
and
As _ is reduced,
stage
has
to 0.15,
for
occurs
by
At
split
At
efficiencies
efficiencies
reaction.
through
In
to 5 percentage
points
obtained
imposing
3-7. turbine
static
turbine
is a much
while
figure
increases
and
turbine
negative
in
percentage
values
the
of 2-stage
As _ is reduced
2-stage maximum
an
efficiency.
of 1-, 1Y2-, and
2-stage
efficiencies
efficiency
previously,
to adjust
a 1-stage
X value
and a 9-percentage-point-higher
turbine.
to
efficiency.
efficiencies
the
stage
stage
in stage
characteristics
compared
_, of 0.50,
shown
possible
in reference
than
As
average
an increase
it becomes efficiency
ref.
the
so as to maximize
of the
parameter, higher
by
of a second
DIAGRAMS
stage,
were the the 81
TURBINE
DESIGN
AND
APPLICATION
(a)
fb)
(a) Velocity-compounded turbine. FIGURE 3-8.--Velocity-vector diagrams Overall speed-work
second
stage,
75:25 are
for
the
also
related
for nuclear
(for
_<0.5)
in reference
6. Equal
assumed.
(derived
cr
Overall
as eq.
Such
split
work of
n
is the
(stator-inlet
number
velocity
to the in such aircraft. of
in which
general
stage
is equal
to stage
exit
were
then
efficiencies static 82
efficiency,
(intermediate
applications
include
production,
and
turbines stages
work
and
composed (for
constant
speed-work
h>0.5) stage
neglecting
Total
and
efficiency
total
and
stage,
from the
are blade
parameters
are
(3-16)
were
obtained
of
as
or last
velocity)
work
consider-
rockets.
stage
of stages.
is axial)
high
due utilized
_,=_ where
is
splits
their
V/STOL
power
zero-exit-swirl stage
turbines.
combination
multistage
and
(2-111))
for
for
hydrogen
and
being
the
used of
(work
of turbines
required.
turbines
characteristics
stages were
are
use
stage
compactness are
applications
stages vapor
turbines efficiency
examined speed
two
their engines
the
turbine. 2-stage
Because
turbines
direct-lift
dictates
turbopump impulse
as many
than
and
of
efficiencies ratio.
), levels
requirements turbines,
The
blade-speed
turbines.--In
more
fan-drive
a low-work
counterrotating
applications
speed
The
the
at low
row,
be
diagram).
of
potential
n-stage ably
would
illustrated
of a blade
advanced and
general,
functions
efficiency lack
in
(b) Counterrotating for special types parameter _, 0.125.
reheat
where
obtained the
static
stage
effect
for
stator
inlet
as functions
stage for
velocity
of X. Overall
efficiencies. discussed
a first
efficiencies
For
in chapter
overall 2,
a
VELOCITY
DIAGRAMS
w
n_'
o+
(3-17)
,
where first-stage
ideal
exit
total
ideal
to exit
total
This
equation
small.
By
J/kg;
Btu/lb
work
the
based
of inlet
on ratio
J/kg;
Btu/lb
work
based
on
pressure,
J/kg;
ideal static
neglects
using
on ratio
pressure,
general-stage to exit
based
pressure,
general-stage Ah_, ,
work
the
reheat
pressure
to
of inlet
total
pressure
of inlet
total
pressure
Btu/lb
effect,
stage-efficiency
ratio
total
which
reference
definition,
6 shows
equation
(3-17)
to be
becomes
Tb
_--
Overall on
total
the
efficiency
basis
1,.4_n
differs
of stage
total
2+1_
only
(3-18)
in that
efficiency.
the
last
stage
is evaluated
Therefore, n
_'--
The are
multistage
efficiency
presented
Figure
3-9(a)
efficiency This function
this
of
ratio, vary
ations
This
large
increases
total
efficiencies
because
of the
Another in terms 2 (eq. ing ratio
with
leaving
commonly
blade-jet
to the across
the
described
the
of stages must
be
(0.1
are
required
on
the
is and
The
vari-
the
concern either
to achieve
high
of stages
static
although
a
blade
or less),
number The
trends,
k----1.
shape
value.
however,
expected.
similar
number,
indicated _, values
at
herein,
to diagram
are,
low
limiting
are
Reynolds
diagrams at
stages
6.
is
efficiencies
at lower
levels
loss. method
ratio. ratio
energy tubine.
all
restriction
show used
speed
kinetic
from
of presenting
parameters
as the
when
addition
manner
reference
of _. The
those
angle,
in
that
if some
3-9(b)
all
(stator
varying
efficiencies
of diagram
(2-72))
as
this
from
as a function
etc.)
number
or,
lower in figure
factors
illustrates in the
shown
well
in
obtained
is reached
as
or downward
figure
obtained
was
efficiency
solidity,
in efficiency
here.
which
0.88)
other
blade upward
imposed,
total
case,
(3-19)
characteristics
3-9,
efficiency,
of many
aspect
overall
figure
shows
(in
level
may
in
1, f n--1,
is to plot This
of the
parameter blade
associated Blade-jet
was
speed with
speed
turbine
efficiency
performance
as a function
described
to a velocity the
ratio
in chapter correspond-
total-to-static is related
of
pressure
to speed-work 83
TURBINE
DESIGN
AND
APPLICATION
11
'_
.S .6_
.....
(_
Number of stages
I
_.... I z l Illl
Limiting efficiency
I
l
I
L
I J I llJl
.8 i_-
.5
•_
.4
32 I/
of stages/ 1
.z( b_
J I = I= I=1
t
.01
.02
.04
(a) Total efficiency. (b) Static efficiency. efficiency characteristics.
FIGURE 3-9.--Overall
parameter
and
From of the effect
the
efficiency
discussions
number on the
specific
(actual
or ideal)
imposed
the
final
selection
among
such
requirements),
compactness,
assumed In 84
the
first
half
to represent
a turbine
of the
design
and blade
goals
structural
type
are very
turbine
from
I
6.)
that
the
selections
have
an important
dependent speed
diagrams
upon
utilized. must
as performance
integrity
ref.
.8
(related
the In
an
represent
(dictated to
by
component
and weight.
RADIAL In
and
.6
(2-74).
it is clear diagram
level
design, cycle
life),
velocity
efficiency
a compromise the
and
section,
.4
(Curves
to equation
expected
work
actual
according in this
of stages
l = 1= I=1
.06 ,08 .I .2 Overallspeed-work parameter,
having
VARIATION of
this
OF
chapter,
average
conditions
a relatively
high
DIAGRAMS
a single over hub-
velocity the
entire
to tip-radius
diagram blade ratio
was span. (about
VELOCITY
0.85
or
lower
greater),
hub-
velocity
such
an
to tip-radius
diagrams
may
or may
blade
span.
ratios,
are
not The
must
important
in
radial
and
be applied final
variations
and
are
conditions
in the
radial exist in section
become will
effect
entire
to the
section
and their
the
must mean
which
This
of
diagrams for
due
end regions,
selection.
case
mean-section conditions
diagrams
to the
the
variations
balance of forces that were described for the
diagram
in flow
the flow
in
the that
In
substantial
average
variations
diagrams
the
however,
the
radial
in blade speed The considerations also
is reasonable.
encountered,
represent
variation the flow.
the
assumption
DIAGRAMS
on
very
consider
the
velocity
diagrams. Radial Consider
an element
3-10(a).
When
sulting
there
force. acting
on the
path.
When
the
force
must
fluid
be accounted
The
is termed
radial
The
radial
The
and
3-10(b))
to
maintain
for
as part
the
to fluid
the
of forces
net
as in figure
be
the
moving
along
along
the
maintained
balance is curved
flow
of the
field,
of velocity,
(streamline)
flow must have radial direction
balance
flow
must
serves
to keep path
by
its curved
curved
path
Any
linear
force.
an associated pressure force, if the streamline is inclined
required
to account
a
centrifugal
(fig. 3-10(c)),
this
pressure
re-
for these
part from
factors
equilibrium. equilibrium
pressure
turbine component
force
through-flow
required
horizontal.
(fig.
pressure
acceleration of the of which is in the
in the
is a tangential flow
The
force the
of fluid
circumferential
pressure
Equilibrium
forces
figure
3-10(b).
in the
x direction,
will
acting
Fluid
weight
the
now
on
net
an
be
formulated
element
is neglected. pressure
force
Fp.,et:(p+dp)(r+dr)dO--prdO--2
mathematically.
of fluid If
unit
are
indicated
length
(directed
radially
(p+?)
dr
in
is assumed inward)
is
sin dO 2 (3-20a)
where F_,
n_
g
net
inward
pressure
P 0
static
pressure,
angle
of rotation,
r
radius
Neglecting setting
of rotation, higher-order
sin
(d0/2)=d0/2
force,
N'm
N;
lb
2; lb/ft _
rad m; terms
ft (product
of
three
differentials)
yields (3-20b)
F_. ,,, =rdpdO The
mass
m of the
fluid
and
being
acted
on by
the
pressure
force
is 85
TURBINE
DESIGN
AND
APPLICATION
!_!ii2iiii!_i!_::: dr
J (a)
p+dp + dpl2-_ P
____
dBI2
.-
Vu e
(-/dr_
_
or_
_
/
/ p+ dp/2
\ \
!p/
rVm.
._____Vx
ame .I vr
(b)
(c) (a)
(b)
Rotation
plane
Element
of
fluid
(c)
FIGURE
3-10.--Radial
reduces
flow
field.
Meridional
equilibrium
m=p[r(r+ which
in turbine
(r-e).
dr)_--wr
plane
(r-x).
factors.
_] d_f0 2r
(3-21a)
to m=--prdrdO
The
net
previously. ferential
pressure To
flow,
force
balance the
the
radial
g
from
centrifugal
pressure
F_,c--m
86
results
Vu _ r
(3-21b)
force
prdrd0 g
the force
three
factors
associated
mentioned with
circum-
is
Vu 2_p V2drd r g
0
(3-22)
VELOCITY
The
radial
component
centrifugal is
force
of the
associated
FT, 0-----m
pressure
with
V_,
cos rm,
g
force
flow
required
along
a,_=
the
prdrdO g
DIAGRAMS
to
balance
meridional
V*. r_
cos
the
streamline
am_
(3-23)
where V,_
velocity
along
r,_
radius
a,_e
angle
of inclination
The
positive
directions
of curvature
are as indicated indicates case. the
the
radial
linear
various
the
plete line
(3-25)
deg
3-10(c).
For
The
of the the
(3-22),
V_ r
Thus,
radial
flow
approximation
as "simple"
those
order
that
(eq.
(3-20(b))
and
(3-24))
convenient flow),
the
angles
(3-24)
equal
to
the
yields
(3-25)
and
includes
to use
in its
meridional
(am,)
all com-
stream-
are
both
side of equation term and can
V_ r
quite
(3-25) often be
(3-26)
equation
Variations
the
nature
there
definition
will
is no (eq.
in
of the
second
assumptions
to be zero,
enthalpy
is
dV,,_ dt - sin a,_
on the right (rotational)
by
are usually
simplifying
assumed total
to illustrate
effects
other
to produce
(3-26)
has
become
known
equilib.rium. Radial
In
required
in this
write
represented
radial
(3-23)
outward
equation
not
inclination
gdp pdr-The
in equation
streamline
equilibrium
(or near-axial
and
we can
angle
V_, dVm_ cos a_e---sin a,_e r_, dt
It is, however,
(1/r,_)
sign
prdrdO g
(3-23),
and inclination
force
meridional
force
ft
is directed
pressure
small. Therefore, the last two terms are small as compared to the first neglected.
minus force
pressure
is the axial
curvatures
curvature
pressure
(eqs.
factors.
form.
streamline,
radial
_gdp p dr--
contributing
of meridional
dVme dt " sin _----
components
Equation
m;
along
net
ft/sec
streamline,
component
Fv • Z=--g
m/sec;
of meridional
balancing
acceleration
Setting
streamline,
for streamline
in figure
that
The
meridional
radial
(1-49))
order be
Velocity radial
variations
will be neglected, made.
If
component can
in velocity,
be written
•
and certain
streamline
slope
of velocity,
and
is the
as
87
TURBINE
DESIGN
AND
APPLICATION
" -- 2gJ-Differentiating
with
substitute
for
dh
respect
(and
dh' ds dr --T-_r-_ If
the
flow
enthalpy
entering
at the
to
since
radius
and
using
equation
(1-8)
to
p= 1/v) yields
1 jp
the
(3-z7)
2gJ
dp dr
1 _ 2gJ
turbine
first-stator
d(V_ 2) 1 dr -_ 2gJ
is radially
exit
d(Vx 2) dr
uniform,
is radially
(3-28)
then
constant.
the
total
Further,
if the
stator loss is radially constant, then the entropy at the first-stator exit is also radially constant. The rotor, as will be discussed later this
chapter,
enthalpy) loss. At
may
extraction any place
enthalpy
and
gradients
imposed
due
to radial
For
or
are
tion
(3-26),
into
equation
and in the
entropy
not probably turbine,
depend
by the
have
radially
constant
does not have therefore, radial
on
the
various
uniformity
blade
rows,
work
radially gradients
of the
in
(total
constant in total
inlet
and the gradient
flow,
the
damping
mixing.
simplicity,
entropy
may
it is here
radially the
assumed
constant.
With
"simple"
(3-28),
that
the
these
radial
total
enthalpy
assumptions
equilibrium
and
and with
expression,
the
equa-
substituted
we get
v. 2 , 1 d(V. 2) 1 -_ 2 In
order
to
specify
a relation
often,
a variation
or, in terms
solve
this
between of swirl
dr
--I-_
equation,
dr
(3-29)
it is necessary
V_ or V_ and
to
r or between
velocity
with
V,,:
Kr N
of mean-section
--0
radius
independently
V,
has
and V_. Most
been
specified (3-30a)
conditions,
v.
(3-30b)
vZ:=,,E: Substituting (3-29)
equation
and
then
V,.,_-V, where
a_
(3-31)
is not
88
is the valid
(3-30b)
integrating
{1--tan' absolute for
the
as
and
its
between
am flow special
differential the
limits
( i)rc,r angle case
at
form
I_\_/
--
the
mean
of N=0
into
of r,_ and
,l
_I}
(3-31)
radius.
(constant
equation
r yields
V_).
Equation For
this
VELOCITY
special
case,
integration
of equation
v=V_=[1--2 A case the
of interest
absolute
and
flow
equation
not
angle
(3-29)
The
radial
is radially
integrates
variations
for
from
a mean
velocity
flow
E
_
_.._>= m_
flow
equation
constant.
V=(r'_
(3-32)
(3-30b) In this
case,
is that
where
V,-=-V=
tan
-sin'a
velocity,
above
angle
In _.j
angle are
of 60 °. largely
(3-33)
axial
velocity,
are
presented
equations,
The
radial
dependent
_
and flow angle, in figure
variations on
the
in
specified
3-11 axial swirl
___"'Exp°nent'N1 0
1.0
]
.5
I
I
- J
2.0 V u = Kr N Q .m
"N
_-2
L.
_ E "- :>_
Vu = KVx 1.C
-1
x
........
B e--
O
60[
30 .7
-1
< .8
I
I
I
.9
1.0
1.1
Ratio of radius to mean radius, FIGURE
3-11.--Radial
a,
to
in swirl
the
radius
and
by
yields r 71/2
tan _ _
covered
Vu
as computed
(3-29)
DIAGRAMS
variations
of flow
angle
velocity a,,,
and
I ""-z 1.2
I 1.3
r/r m
flow
angle.
Mean-section
60 °.
89
TURBINE
DESIGN
velocity increases and
AND
APPLICATION
variation (value of N). As the swirl distribution exponent N or decreases from a value of --1, the changes in axial velocity
flow
angle
with
changing
seen, the axial velocities of N cannot be obtained can
be used
shorter
for design
(values
variations
purposes
of rh/r,,
and
illustrated
discussed
radius
become
and flow angles with all blade becomes
rt/rm
in figure
in subsequent
When
a value
stage
of this
Free-Vortex of -- 1 is used
as the
to 1). The on
pronounced.
As
with certain values The range of N that
larger
closer 3-11
sections
more
associated lengths.
blades
effects
become
of the
velocity
radial
diagrams
are
chapter.
Diagrams
for the
exponent
N in equation
(3-30a),
then rVu=K This
is the
for
such
condition a swirl
in a free
distribution
or a free-vortex The turbines
for flow
to
and as
a turbine
designed
a free-vortex
design,
turbine.
free-vortex in which
products
Thus, valid
vortex,
is referred
design is used radial variation
this condition is specified at there is no radial variation UVu
(3-34)
both
entering
in the of the
both the stator and rotor in specific work, _x(UV_),
and
leaving
the specific work computed for the entire flow. Further,
axial
velocity
mass from
flow per unit area the mean-section
Vx
entire
flow
design
simplicity
is radially
within
vortex
designs
An
example
rotor
from the if N=--I
constant.
accuracy
of
of the
main
is one
for axial-flow of
the
outlets, because
are radially
constant.
mean-section in equation
Thus,
the
then the
diagram (3-31),
radial
is the
variation
in
(pV_) is small, and the mass flow rate obtained velocity diagram can be used to represent the
an
set
vast majority of axial-flow diagram is accounted for. If
0.1
percent
reasons
in
for
most
the
cases.
wide
use
This of free-
turbines.
velocity
diagrams
for
a
free-vortex
design
is
shown in figure 3-12 for the hub, mean, and with a radius ratio of 0.6. The radial variation
tip sections of a blade in the diagram shape
is
for
considerable.
The
symmetrical )_m of
zero-exit-swirl
1. The
(_h=0.56), reaction hub
(lowest blades, 9O
while
the
(_t----1.56). is the
efficiency). the in order
diagram
diagram
associated
section
selecting
mean-section hub tip
diagram
Thus, critical
for
to ensure
special diagram,
satisfactory
an
swirl
care
is diagram
with
high
distribution,
must for at the
a
parameter
impulse
aerodynamic
especially diagrams
an
conservative,
free-vortex from
example
a speed-work
is nearly is very
a
section
Therefore,
mean-section
having
diagram
this
the
standpoint
be
taken
when
low-radius-ratio hub
section.
A
VELOCITY
DIAGRAMS
45. 30....
Radius ratio, rh/r t = O.6
Hu_ section
rm/r t ° O.8
Mean section
rt/r t = 1.0
Tip section 3-12.--Radial variation flow. Stator mean-section exit eter Xm, 1.
of velocity-vector diagrams for free-vortex angle a,,, 60°; mean-section speed-work param-
FIGURE
very
high
increases Another
reaction
to
diagram
leakage across the potential problem
considerable trated
tip
radial
in figure
--38 ° at the
an overhanging bending stresses. blade is illustrated
tip,
the
in rotor rotor
a variation
tip section,
also
be
troublesome
because
blade tip clearance space. is that of rotor-blade twist.
variation
3-12,
can
thus
The positioning in figure 3-13.
inlet
inlet angle
of 83 °. This causing of the
some hub
angle.
For
varies
from
results tip
case
hub
having
problems sections
is a illus-
45 ° at the
in a blade
fabrication and
the
There
it
and
of such
a
91
TURBINE
DESIGN
AND
APPLICATION
.-/*-
_ ip section
\\
n
FmURE
3-13.--Relative
positioning
of hub
and
Non-Free-Vortex Free-vortex are often
designs
classified
non-free-vortex potential trated
the
vortex design
1.111, the
r/r,_
sections,
to the
3-11,
3-14
no real
At
any
swirl
having The
For
a blade
of 0.889
mean
section.
for those
exit
blade
particular
exist
ratio, swirl
constant-flow-angle
There
the
rotor
cases superwheel-
the
constar_t-flow-angle
--1)
design.
The
r/r,_ of 1, are
radius
ratios
mean-
the
same
r/r,_ of 0.75,
to tip-radius to the
ratio
hub
and
to tip-radius
ratio
to the
and
hub
ratio
decreases,
to a blade
section
relatively
no
for which,
Gf tip
to tip-radius
of course,
of tip
a hub-
cases
for axial
Illus-
for the
correspond
hubare,
design.
the
correspond
with
The of the
The
a hub-
of r/rm corresponds
values
radius
at
arLd 1.111
As the
value
1.25
some
3-11.
(N:
with
vortex.
to alleviate
design,
and
diagrams
of non-free
(N=0)
ratio
a blade
designs
in figure
free-vortex
and
turbine.
other
in diagrams
at a radius
of 0.75
distributions. zero
are For
respectively.
in figure
92
values
particular
the
design,
all
free-vortex
constant-swirl
are
shown 1.25.
r/r,_ values
sections,
the
Also and
respectively.
the
closer
with which
the
variations
illustrated
the
of freeovorgex
that
heading with
(N=I)
compared
used
in an attempt
radial
variations
solid-rotation,
all cases.
any
the
design,
diagrams,
0.889,
common
used
associated are
velocity
are
section
0.8,
3-14
(N-------2) or
0.6,
the
sections
Diagrams
so commonly
are
disadvantages
having
for
under
designs
in figure
flow,
are
tip
diagrams
to show
as shown
in figure
velocity. exit
diagrams
This is due to the selected
are
the
same
mean-section
for
all
diagram
(az._:0). diagrams
are
quite
similar
to
the
free-
VELOCITY
DIAGRAMS
Radial swirl distribution
Ratio of radius to mean radius,
Super vortex (N = -2)
Free vortex (N = -l)
Constant swirl (N = O)
Wheel flow {N = 1)
(a)
(a)
Constant flow angle
rlr m
1. 250
(a)
1.111
1.flOf
O. 889
O.150
(a)
aNo real value for axial velocity. FIGURE
3-14.--Radial
vortex
diagrams
rotor-blade the
variation
and,
twist
and
therefore, low
constant-flow-angle
stator
has
The
a small
sort.
The
case.
The
radial
present
hub
amount
of twist
(N= blade
has
--2)
twist
variation
The
constant-swirl
alleviate
the
design.
is more
large
and
below
cannot
about
0.85
for
and
relative
than
for
turbines, those
blade-twist
the
0.70
be sustained
velocities these
too
for the
wheel-flow
the
and
here
free-vortex higher
of a free-vortex
severe
(N= at
the
flow
blades
with
hub-
stator
exit For
velocities
are
could
velocity about
absolute
these Mach
higher
is
ratios
below hub
for
high
do
free-vortex
axial
the
higher cause
diagrams
and
addition,
can-
to tip-
to tip-radius
design
relatively
and
hub-
of the in
of
free-vortex
with
(N--l)
(N=O) In
the is large
problems
1) design.
design.
for
variation
on blades
is that free-vortex
no advantage
velocity
wheel-flow
constant-swirl
the
to have
on
radial
of high
advantage
than
axial
hub-reaction the
swirl
12°).
imaginary) and
various
problems
while
appear
of stator-exit
(N=0)
However,
twist,
(about
for
same
A possible no
diagrams
not be sustained (Vx becomes radius ratios much below 0.8.
diagrams
the
reaction.
stator
super-vortex
any
of velocity-vector distributions.
designs number
losses
than
design. 93
TURBINE
DESIGN
AND
APPLICATION
M - 0.58
M/_ =o.sr - 0.77/ 4z" M
-8
Tip section, rlrt = 1
Sectionat r/rt - O.68 (a)
16. 6°--__
_r \
_ "_'_ Mr "0./_,_
M,.oW Mr" 1"01_'_
_45.
3o
_'" &'i_
-\
I1__, "7°
/M-
0.74
Sectionat rlr t - O.67
Tip section, rlr t- 1.0 (b)
FmURE
94
3-15.--Comparison twisted
(a) Free-vortex turbine. (b) Nontwisted turbine. of velocity-vector diagrams of free-vortex turbines. (Diagrams from ref. 9.)
add
non-
VELOCITY
A design termed
procedure
for
a "nontwisted"
design
completely
should
be easy
results
exit tions
_. Although
rotor
10 ° for
free-vortex
design.
At
the
at the
tip.
The
for the
same
with
vaIiation
7.
exit,
the
relative
stator
designs.
swirl
at
design
Mach
(0.85)
than
has
stator
from
and
the
hub
free-vortex
of
nontwisted
hub
at
value
increased the
at the
The
condi-
(N)
number
for the
the
stator-exit
30 ° for
is negative
blade-inlet
a
9 are shown
velocity
twist
than
Such
therefore,
of reference The
angle,
experimental
nontwisted
in axial
to more
exit
which,
9 contain
design.
is eliminated, design
rotor
rotor,
study
nontwisted
and
in reference
the 8 and
the
inlet
to a swirl-distribution-exponent
twist
nontwisted
However, over that
for
radial
in this closely
in
designs
used
A large
correspond the
is presented twist
free-vortex
present
of constant
References
diagrams
3-15.
is also
design,
to fabricate.
velocity
in figure
blades
eliminates
comparing
design
positive is higher
design
(0.72).
the reaction at the hub of the nontwisted design is improved of the free-vortex turbine. The two turbines have about the
efficiency.
The
non-free-vortex
work
and,
tion
because
in mass
tions
may
error
may
section by
rotor
DIAGRAMS
occur
if such
As
seen
from
free-vortex Mach
conditions
and
flow
rate.
this
It
designs
been be
from
used
increased
has
cannot
deviations
results
to obtain
than
design the
in
use
other
stator
sustained
basis and
of the
mean-
be designed
tip
in
order
to
of a non-free-vortex the
design
procedures,
of a free-
however,
of m_n-free-vortex
problems
this
over
all
to with
higher design
from
spans.
as reported
turbine
as
increased
deviations blade
designs associated
such
and
large
designs,
PROGRAMS
problems
twist,
that
improved
COMPUTER
design
considerable
should
hub
hub-reaction
shown
free-vortex
on the
proper
variacondi-
disadvantage.
discussion, and
and
turbine
complex
computerized
rotor-twist
numbers,
The more
is no real
designs
plexity.
been
much
radial
mean-section
conditions,
between
in specific
velocity,
the
is designed
flow
With
the
Thus,
average
a turbine
variation
in axial
area.
the
complexity
alleviate
radial
A non-free-vortex
therefore,
turbine.
additional
feature
gradient
unit true
conditions.
work
all
radial per
represent
is,
vortex
rate
not
integrating
turbine
of the
flow
flow
compute
designs
hub com-
free-vortex
However,
in reference
small 10, have
performance.
FOR
VELOCITY-DIAGRAM
STUDIES This diagram
chapter
has
selection,
staging,
and
the
diagrams
best
radial
presented including variations.
and number
some diagram
of the
basic
aspects
types,
their
relation
It is evident
that
the
of stages
for a given
of velocityto efficiency,
determination
application
of
requires 95
TURBINE
many
DESIGN
tion. such
then
One such The program radial
is
computer
computer includes
allows
program
uses
reflects
equation
and
real
exit
dependent
the
in reference
(swirl
14,
ef swirl
proven
very
wherein
to
any
an internal a basis.
rotor
work
However,
of
velocity)
loss This (which
for
either
a
with
The
it not
13 as
(Vme=V_/cos
because
12. in and
addition,
includes
inputs.
perform
11 and effects
specifications,
velocity).
many there
a,,_)
large
is
or
the
variation
small
in
variations
existence
of
these
in condi-
3-11. in
the and
a program
radial
is used
successful
with
as
calcula-
in enthalpy In
and
velocity
resulted
velocity
also
input
(meridional
has
instead
variation
evolved
reference
distribution
solution
by figure
problem
generated
swirl
meridional
variable
is indicated
radial of hand
gradients
but
distribution
find
variable
independent
and
in flow.
from
of these
for
cannot
radial
as an input
swirl)
solution
non-free-vortex
realm
been
variations
information
combinations
computer
This
loss
the
exit
effects, of the
have
and
radial
stator
rotor
values
include
program is described in references consideration of streamline-curvature
for blade using
to
are out
programs
in determining
correlation
desired
analyses
equilibrium
entropy
tions
it
curvature
such
Therefore, tasks.
only
If
meridional-streamline
in efficiency,
no
APPLICATION
considerations.
designs,
the
AND
variation
as input.
shows
reasonable
modification,
that
in
The
meridional
modified
valid
variation
as reported velocity
program
turbine
designs
in meridional
has can
be
velocity.
REFERENCES 1. STEWART,
2.
WARNER
teristics
in
ASME,
Dec.
STEWART,
L.:
Terms
A Study
of
of Axial-Flow
Velocity
Diagram
L.:
Analytical
4.
WILLIAM T.;
WINTUCKY,
Characteristics
of
Terms
and
of Work
ments. 5.
NACA
WINTUCKY, ments.
RM
Paper
Turbine RM
Charac61-WA-37,
WARNER Turbine
with
WILLIAM
Requirements.
Analysis
of Efficiency
Downstream T.:
RM
Analysis
of Work
Stators
E56J19, and
in
1957.
of Two-StageSpeed
Require-
1957.
Efficiencies
E57L05,
Speed
L.:
NACA
in Terms
Single-Stage-Turbine
and
ANY STEWART, WARNER in Terms
L. : Analysis of Work
and
.of Two-Stage Speed
Require-
1958.
L. : Analytical 1958.
of
Work
Requirements.
E57F12, T.;
Characteristics E57K22b,
of
STEWART,
Single-Stage Speed
RM
6. STEWART, WARNER ciency
Terms
Characteristics
WILLIA_a
NACA
AND
Investigation
L.; AND WINTUCKY,
Efficiency
Counterrotating
96
a
STEWART, WARNER Turbine
Efficiency
1961.
WARNER
Efficiency Characteristics in NACA RM E56G31, 1956. 3.
Turbine
Parameters.
in Terms
Investigation of Work
and
of Multistage-Turbine Speed
Requirements.
EffiNACA
VELOCITY WILLIAM R.; AND SILVE_RN, DAVID H.: Analytical Aerodynamic Characteristics of Turbines with Nontwisted NACA TN 2365, 1951.
DIAGRAMS
7.
SLIVKA,
8.
HEATON, THOMAS R.; SLIVKA, WILLIAM R.; AND WESTRA, LEONARD F.: Cold-Air Investigation of a Turbine with Nontwisted Rotor Blades Suitable for Air Cooling. NACA RM E52A25, 1952.
9. WHITNEY,
WARREN
J.; STEWART,
WARNER
L.;
AND
Evaluation of Rotor Blades.
DANIEL
MONROE,
E.:
Investigation of Turbines for Driving Supersonic Compressors. V-Design and Performance of Third Configuration with Nontwisted Rotor Blades. NACA RM E53G27, 1953. I0. DORMAN, T. E. ; WELNA, H. ; AND LINDLAUF, R. W. : The Application of Controlled-Vortex Aerodynamics to Advanced Axial Flow Turbines. J. Eng. Power, vol. 90, no. 3, July 1968, pp. 245-250. 11.
CARTER,
A. F.; PLATT, M.; AND LENHERR, F. K.: Analysis of Geometry and Design Point Performance of Axial Flow Turbines. I-Development of the Analysis Method and the Loss Coefficient Correlation. NASA CR-1181, 1968.
12.
PLATT,
M.;
formance 1968. 13.
SMITH,
vol. 14.
AND
CARTER,
of Axial
Flow
A. F.:
Analysis
Turbines.
S. F. : A Simple Correlation 69, no. 655, July 1965, pp.
of Geometry
II-Computer of Turbine 467-470.
and
Program. Efficiency.
Design
Point
NASA J. Roy.
CARTER, A. F.; AND LENHERR, F. I_.: Analysis of Geometry Point Performance of Axial-Flow Turbines Using Specified Velocity Gradients. NASA CR-1456, 1969.
Per-
CR-1187, Aeron.
Soc.,
and DesignMeridional
97
TURBINE
DESIGN
AND
APPLICATION
SYMBOLS A
flow
area,
m_; ft 2
pressure conversion
g h
force, N; lb constant, 1 ; 32.17
(lbm)
J
specific enthalpy, J/kg; Btu/lb conversion constant, 1;778 (ft)(lb)/Btu
K
proportionality
L
loss,
m
mass,
N
swirl
(ft)/(lbf)
constant
J/kg;
Btuflb
kg;
lb
distribution
exponent
number
of stages
P R
pressure, reaction
N/m_;
r
radius,
8
T
specific entropy, temperature, K;
m;
lb/ft 2
ft
U
blade
V
absolute
speed,
t)
specific
volume,
W
relative
velocity,
W
mass
flow
o_
fluid
absolute
J/(kg) °R
m/sec;
velocity,
(K) ; Btu/(lb)
ft/sec m/sec;
mS/kg; m/sec;
rate,
(°R)
kg/sec; flow
angle,
ft/sec ft3/lb ft/sec lb/sec deg
efficiency 8
angle
k
speed-work
of rotation,
deg
parameter
density,
kg/ma;
lb/ft 3
Subscripts: a
first stage annulus
c
component hub
h i /d
general ideal
1
component
m
mean
me
meridional
net
net
r
radial
ro
rotor
8
component
st
stator stage
98
due
to circumferential
due
to linear
flow
stage acceleration
section
component
due
to streamline
curvature
(sec 2)
VELOCITY
t
tip tangential
_g
DIAGRAMS
component
0
axial component at stator inlet
1
at stator
2
at rotor
exit
or rotor
inlet
exit
Superscripts: --
overall
'
absolute
turbine total
state
99
CHAPTER 4
BladeDesign By Warner L.Stewartand ArthurJ. Glassman The
design
of a turbine
determination are usually the
overall
established
by
evolution
and/or
of velocity
number
is the design required This The
shape,
height
of the state
fluid
usually
The
assure
chord
many
chapter.
chord
and
by the
or axial profile
as well as the of this
used
third
and
step
velocities of
with
to allow
operation.
flow
mechanical
con-
selection
of blade (ratio
chord
to spacing), first
blade
exit
is then which profile
part
and
inlet
discussed is the design,
is
fabrication
in the
profiles, the
chord
as solidity
theory,
to accomplish
speed, dictates
blade
accurate
The
of axial
includes
which
The
consistent
design.
of flow,
diagram,
turbine.
enough
(ratio
of blade
requirements
will be discussed
surface
Channel
is
the determination
nondimensionally
which
connecting
chapter.
procedures
value
solidity
design,
step efficiency
3. The
aspects
velocity the
during
that
is the These
second
desired
flow angles
important overall
be long
be expressed
the
involves
first
speed.
blades.
throughout must
the
in chapter
step
the selected
integrity
can
part
next
of the
to be a minimum
tries
in the
This
The and
The
with
will produce
of the more
is set
considerations
Blade
analytical
that
some
blade
to spacing)
volves
discussed
was
steps. work,
application.
This
spacing
structural which
particular
consistent
conditions
selected
spacing,
the
major of flow,
diagrams
diagrams.
conditions
state
siderations. and
and covers
of three
requirements
of the blading
chapter
and inlet the
of stages.
by the velocity
the size,
consists
of the
inof this
geome-
in the
basis
of
last
for
is discussed
chapter.
_A_}l___
i_._f,9_i.(L
the
Y _,. A_
TURBINE
DESIGN
AND
APPLICATION
SOLIDITY One
of the
important
of the blade
solidity,
A minimum
value
weight,
cooling
mechanical
flow,
the
aerodynamic
will include
description suppress
between
separation
Figure
4-1
as the
static-pressure
figure
are
pertains equations
and
rows rather used
must
inlet
tions,
and
If one height
rows
stages,
in previous are
and
taken
The
as negative
negative
if in the
considers
the
same
blades,
from
blade
in this
bla(t(_ rows. absolute
When
will differ
The
as well in this chapter referring
velocities
concerned
inlet
components
in the
with
blade
slightly
from
component
values
are positive
ar_ in opposite
direc-
direction.
then inlet
velocities
tang(_ntial-velocity
values.
two-dimensional
two
solidity.
The
convention
tangential-velocity
for use to
discussion
we are
exit
dis-
will be a
studied
ai_d (,xit diagrams
than
chapter
The
on solidity
Solidity
a blade.
rather
in
will concern
Also included
on
by
results
selection.
permissible
The
the angle
chapters.
exit
as it flows
around
is limited
requirements
inlet
velocities.
to spacing. of reducing
section
are being
as well as to stator
with
than
of blade
in this
This
solidity.
the
selection
eventually
solidity
Diagrams
relative
Since
between
fluid
reduce
figures.
flow angle
if the
thereby
use
flow.
that
chord
reduction
spacing
and
concepts
is the
standpoint
diagram
loading
distribution
blade
we
or axial
the
affecting
blading
set
design
chord
of velocity
as absolute
to rotor
to a rotor,
factors
a typical
shown
from
increased
of Velocity
shows
of chord
However,
blade
and
blading
to separated
the effect
Effect
and
cost. due
of advanced
ratio
desired and
efficiency
and the relation
that
is the
and
blade
with
cussion
which
of turbine
is usually
considerations,
decreased itself
aspects
flow the
through
tangential
(subscript
a passage
force
1) to exit
exerted (subscript
of unit by
the
2) is
1 F,, =-
smV.,2(
V,, ,_- V,_ ,_)
(4-1)
g
where Fu
tangential
force,
conversion 8
blade
P
density, axial
Vu
tangential
This due
lb/ft
component
forc_
(Ibm)
(ft)/(lbf)
(see 2)
s
of velocity,
component
lower
m/see
of velocity,
exerted
to the static-pressure 2. The
1; $2.17
m ; ft
kg/m'_;
tangential
in chapter 102
constant,
spacing,
V_
N; lb
by
the
distribution part
of figure
; ft/s(,c m/see;
fluid
must
around 4-1
ft/sec b(, _h(_ sam(, t h(_ blade,
shows
a typical
_s the
as was
force
discussed
static-pressure
BLADE Stations
DESIGN
1
surface-'" "_ /- Such'on'_--r-
Vx, 1
--L y2_Vu,
.,_-_...._
2
C X --------_
pl
P
Pl
13-
P2. "'" rs, mln Axial distance
FIOUP, E
4-1.--Typical
distribution between
around the
flow in the
two
tangential
blade-row
the blade curves
velocity diagrams distribution.
row as a function
represents
direction.
the
and
of axial
total
blade
surface
static-pressure
distance. force
acting
The
area
on
the
Thus,
F,, = c_
L'
(pp-
p_) d
(4-2)
where C_
axial
Pv
pressure-surface
P,
suction-surface
X
axial
The
axial
chord,
distance,
solidity,
m; ft static static
pressure,
N/m2;
pressure,
N/m2;
lb/ft lb/ft
2 2
m; ft ¢z, is
{T x
_-
--
(4-3)
8
103
TURBINE
DESIGN
Substituting
AND
APPLICATION
equations
(4-1)
and
(4-2)
into
equation
(4-3)
then
yields
a_ =
(4-4)
/0
g At this point, been
used
first
is the
to relate
and
pressure
blade
surface
loading
that
pressure.
In equation
t'
equal
blade
Zweifel (l)
have
loading. (ref.
This
pressure
total
to be constant
The
1).
the static
to the inlet
surface
that
pressure and
equal
form,
(pp--
_, =
by
assumes
and
oil the suction
coefficients
to an ideal
introduced
to be constant
pressure
loading
loading
coefficient
on an ideal
static
exit static
two tangential
actual
used
is based
(2) the
to the
the
widely
coefficient on the
we introduce
d
p.)
d (4-5)
pl' -- p_
where Zweifel
_Z
loading
coefficient
pl r
inlet
total
pressure,
N/m2;
lb/ft 2
P_
exit static
pressure,
N/m2;
lb/ft
The
second
constant
coefficient
static
is similarly
pressure
on the
value
of static
pressure
(see
cient
can never
exceed
a value
ahvays
be less than
ceed a value fined as
2
1. The
defined
suction
fig. 4-1)
of 1. In equation
on that
of 1, and
Zweifel
surface.
(pp--
loading
the
assumed
to the
This
minimum
loading
purposes,
on the other
this second
/o
that
is equal
for all practical
coefficient,
form,
except
surface
coeffiit must
hand,
coefficient
can
ex-
_b is de-
p_) d (4-6)
pl p-
where p,,m,, is the N/m 2 or lb/ft2_ _. The pressed
velocity
minimum
components
static in terms
ps
,min
pressure
on
of veloerity
the
suction
and
flow
surface
angle
are
in ex-
as V_ = V sin a
(4-7)
V_ = V cos a
(4-8)
and
104
BLADE
DESIGN
where V
fluid velocity,
ot
fluid flow angle,
Substituting (4-4)
m/see; deg
equations
and
using
the
ft/sec
(4-5)
or
(4-6),
trigonometric
(4-7),
relation
mVQ
K is the
inlet
to that
1) sin 2a2
of tangential at the
flow
and
with
Bernoulli's
blade
equation
1) sin 2a2
component
(Vu.1)
relations.--Relations are
(4--9)
at the
blade
With
usually
this
involving
evolved
by
assumption,
solidity,
assuming
density
incom-
p is constant,
equation 1 P-k--z pV 2 zg
P'=
can be used.
into
exit.
loading
no loss.
(K-
velocity
of incompressible-flow
diagrams,
pressible and
ratio
(V,.2)
Derivation velocity
(4-8)
VQ (K-
where
and
sin 2a = 2 sin a cos a yields
Substituting
equation (K-1)
(4-10)
sin2a2
-
(4-10)
into
equation
(K-1)
(4-9)
yields
sin2a_
(4-11)
¢ ,,W,, where
V_
Let
is the
us now
velocity
define
on the
suction
a suction-surface
surface
diffusion
where
p = p_._,.
parameter
D, as
D_ =
(4-12) V_ 2
Many parameters the deceleration indication this
of this type have been of the flow on the suction
of the
definition
susceptibility
(eq.
(4-12)) (K-
of the flow on the in equation
Equation
(4-13) for each
coefficient can be seen
_, which that
shows particular cannot
decreasing
(4-11)
1) sin 2a2
_ =
constant
used to represent a measure of surface. This deceleration is an
(K-
blade
to separate.
1) sin 2a2
=
that
the
solidity
velocity-diagram exceed
a value
solidity
results
Using
yields
(4-13)
parameter
a,_D,
requirement. of 1, does primarily
not
or
Since vary
in increased
a,_,
is
loading
greatly,
it
suction105
TURBINE
DESIGN
surface
diffusion
later
in this
gential
AND
(higher
chapter.
velocity
4-2(a).
of K=-
represents and
exit
solidity sents
K
for
an
in the
there
is no turning K
is to be avoided,
from
value
of K, a xnaximum
exit angle
reaction
same
solidity
must
of solidity
(4-13)
to yield
the
can
be
equation
modified
For brevity,
derived
shows
that
the
angles
COS
o_2
_z
COS
O/1
of the
several
values
exit
angle,
solidity
inlet
which
of most
angle
inlet
encountered (4-13), repre-
parameter
suction-surface velocity
diagrams
for
any
is obtained
given
with
was defined
can
inlet
interest
an
with
and
exit
(4-14)
coefficient
can
angle
_,.
Equation
be expressed
is plotted
in terms
against
in figure
with
solidity
exit
4-2(b).
increasing
0 °, a2 <-45°),
decreasing
be evolved,
in chapter
_
flow
inlet
1.
of the
increases
(m>
of the
a2)
parameter
parameter
decreases
relation
in terms
parameter
Solidity
for
region
only
solidity
angle
A third
are
that
parameter
sin (m--
only.
given each
1
solidity
as the
be seen
in reference
2
this is expressed
flow
In the
of K <-
for K = 1. This
to a function
ax-
(4-14)
a
equation
if excessive
can
inlet,
of 45 ° .
Equation
of the
and
angles
increase
in figure
axial
a value
As seen from
It
tan-
of K represent
direction
Thus,
impulse.
value
and
the
angle
with
of the flow. The
values.
toward
flow
values
to zero for all exit
decreasing
move
blade,
blades.
against
blade
Positive
of rotor
is equal
of exit
a reaction
impulse
will be discussed
is plotted
values
blade.
velocities
the case where
diffusion
several
reaction
of which
parameter
1 represents
parameter
angles
solidity
in the tip sections
with
consequence
represents
tangential
increases
the
of K=0
a negative
primarily
D,),
The
ratio
A value
value
APPLICATION
flow For
inlet
a
angle.
parameter
for
exit. angle.
this
one
in terms
of blade
reaction
R,
2 as Wl 2
R--l----
(4-15) V= 2
Substituting
equation
(4-8)
into
R=
equation
1-(
the
two-dimensional,
Substitution
of equation
back
(4-16)
al/
incompressible-flow (4-16)
yields
c°s a2_ 2 \cos
for
(4-15)
into
case, equation
where (4-14)
V,a=Vx,2. then
yields
2 _=-wkere 106
Aa is m--a2.
-x/l-Z- R sin Aa
(4-17)
BLADE
DESIGN
Exit-flow angle, m
% deg
x O
-45 __ X tD t..
E
-75 or -15 -60 or -30
1--
(a) O
°.5
3F
I
I
I
J
0 -.5 -1.0 Tangential velocity ratio, K
_lnlet-flow
-1.5
angle,
Y, I -30
-45
-60
-75
Exit-flow angle, % deg
3 [--
Turn ing angle,
!
z_ deg
, g
,_
2__--_...._
0 -.25
0
.25 .50 Reaction, R
or 120
.75
I.O0
(a) Effect
of tangential-velocity ratio and exit-flow angle. (b) Effect of exit- and inlet-flow angles. (c) Effect of reaction and turning angle. FIGURE 4-2.--Effect of velocity diagrams on solidity.
107
TURBINE
DESIGN
Equation
(4-17)
reaction
and
reaction that,
AND
expresses
turning
values The
of 90 ° and
turnings Radial
parameter
in terms
of blade
parametor
is plotted
against
of turning solidity
varies
angle
the
in figure
solidity
little
with
4-2(c).
parameter
parameter
variation.--Chapter that
radial
varying
must
It can be seen
decreases
is a maximum
turning
unless
hub-to-tip-radius
with
for
very
solidity
nature
high
or very
low
swirls),
turbine
ratio
of 0.7, an impulse free-vortex
hub
and
from
tip
and
equation
the
hub
speed
vary
in the
axial
with
with desired
inlet
and
For
this
exit
ease,
shown
in the
following
table:
Rotor
Exit
Solidity
Inlet
Exit
angle,
angle,
parameter,
angle,
angle,
deg
deg
ffx_z
deg
(leg
ffz_
Hub
0
- 70
0.64
54
--54
1.90
Tip
0
- 62
--2
--63
again
what
different
that
negative.
constant
the
assumption
convention
that
Assume
radially.
.83
angle
from
of previous
that This
enables
the is
us
the
solidity-parameter
Inlet
Note
exit
a constant
a stator-hub
distribution. are
to
velocities,
corresponding
(4-14)
blade
will be illustrated
having axial
rotor
swirl
shown variation
variation
constant
in velocity
varying
Stator
are
in-
a turning
variations the
was
of this radial
a single-stage
°, and
radial both
will be a radial
exit
at the
computed
axial
and
of -70
angles
The
the
to satisfy
there
Consider
inlet
flow angle
Since
solidity.
(zero
values
in order
diagrams,
by an example. flows
3 discussed
occur
equilibrium.
velocity of axial
flow
solidity solidity
are used.
diagrams
value
the The
previously,
reaction.
angle
and
angle.
for several as indicated
creasing
APPLICATION
to
a
being
used
chapters.
loading
in this
Herein,
coefficient
reasonably
proportion
z
.79
chapter stator
is someexit
angles
_b_ is to be maintained
desirable solidity
Solidity parameter,
condition,
directly
to
and the
the
solidity
parameter. Let us now determine shown solidity radius 108
in the
preceding
variation (because
how table
in any blade
the
hub
and
can bc made
blade
spacing
row
must
is directly
tip values
of solidity
physically
consistent.
be
inversely
proportional
parameter The
proportional to
radius)
axial to and
directly proportional to parameter
at the
corresponding
hub
tip
0.64X0.7=0.45, a considerable
axial
chord
chord.
is 0.64.
value
which
fore,
axial
If axial
of
the
can increase
with
chord
half
taper
the
axial
is almost
axial
For
radius
were
tip
axial
desired
solidity
constant,
parameter
to hub
and yield
the
held
solidity
of the
from
stator,
value
is often
the be
of 0.83. used
the higher
then would
There-
so that
solidities
the
desired
at the tip. In the
case
If axial
of the
chord
axial
solidity
than
the
often
used
radius
rotor,
were
held
desired yield
the is not
cally
from
desirable
fabrication axial this
there
solidity radial
where turbine
variation
the
axial
solidities
especially
a radial in loading
blading
is not
axial
taper tip.
hub
with
Taper
desirable,
but
blade
for smaller
turbines,
axial velocity
cases,
is
hub
to
To simplify
mean-section have
to tip increasing
is also mechani-
stress. coefficient.
will not
of the larger
from
in loading in many
loaded,
is 1.90.
is still
from
of reducing
of the
hub
tip value
which
can decrease at the
cocfficient
highly
1.33,
chord
variation
on the basis
at the
corresponding
desired
standpoint
cases,
results
selected
the
1.90X0.7=
only aerodynamically the
in many
and
parameter
Therefore,
so that
lower
tip in the rotor
be
of 0.79.
blades
solidity then
would
value
in rotor
axial
constant,
parameter
and
used,
the
taper
is not
With
the
diagrams,
especially
a severe
those effect
on
performance.
Effect
of compressibility.--Thc
term
pl r-
in equation
(4-9)
shown
by equation
loading
coefficient
by equation
reduces
to 1/D,
(4-13).
For
p*,min
for incompressible
a compressible
¢ as for incompressible
(4-13)
flow
conditions,
flow case having
flow,
division
of equation
as
the
same (4-9)
yields
1 2g t_ V_D' O"x
(4-18) _*,inc
where
ax,,,c
is the
incompressible
equation
such
between
critical
velocity
(1-61),
(1-63),
and
equation
(4-18)
plt--
as (4-13),
(4-14), ratio,
(1-64))
is modified
Ps,,nin
flow
value
or (4-17). density,
and
using
as
determined
By introducing
and
pressure
the
definition
(eqs.
from
an
the
relations
(1-3),
(1-52),
of D, (eq.
(4-12)),
to 109
TURBINE
DESIGN
AND
APPLICATION
0"2:
O'X
(4-19)
, inC
7'+1
V-c, 2
where 7
ratio of specific heat constant volume
Vc.
critical
velocity,
m/sec;
by using
binomial
expansion
Then, equation
(4-19)
at
constant
pressure
to
specific
heat
at
ft/sec and
can be approximated
by neglecting
the
secondary
terms,
as
O" x
- 1
e
a_,,._ The (V
approximation
Vcr)_ values
ratio
diffusion
in figure
as D, either
4-3.
effect
required
for any
solidity
1.50
equation
solidity
value
decreases
effect
from
(4-20)
ratio
for several
compressibility
or decreases
(4-20) 2(7+1)
by
1. The
parameter
The
increases
compressibility 2, the
represented
up to about
suction-surface
_'+1
a value
of ( V with
is quite
values
of critical
becomes
more
values
1.2 .__1. 25 O
1.0 .6 0
110
1
I
2 3 Suction-surface diffusionparameter,Os
4-3.--Effect
of compressibility
on
axial
solidity.
is no
of less than of
Exitcritical-velocity ratio, (V/Vcr)2
FIGURE
velocity
pronounced
V,r) 2. For D, values increasing
for
against
of 2. At D, = 2, there
--
.50
good
_x/¢=._,_ is plotted
(V/Vc_)_.
BLADE
For
Do values
because
of more
it is beyond
than the
2, a region
limits
of good
increases with increasing (V/V_r)2. should be maintained below about Relation It is well recognized pressor
blade
is an
Correlation described This
that loss
in reference
parameter
reflecting
and
a
terms,
solidity.
energy
is defined
neglect
that
the
and
pressure
(Vp.,,i,
pressure
=0),
then
the
overall
D-
V,_.,-
the
or of a comreaction.
parameter
was
compressor
field.
and the second
diffusion 3, where
sum of the
surfaces
surface
ratio
D, values
and
reaction
analogous
of the
blade
within
in reference
ratio
solidity
solidity
diffusion
widely
An
as the
on the suction
is assumed
of both
one reflecting
for the case of the turbine
parameter
the
of a turbine
compressor
is used
two
practice,
interest
to Solidity
loading
with
of academic
Experience has shown that 2 to avoid excessive losses.
function
2 and
includes
turning
evolved
the
is only
design
of Loss
important
of blade
that
DESIGN
parameter
an overall
decelerations
to the exit
in kinetic
kinetic
minimum
velocity
diffusion
parameter
was
diffusion
energy.
is low
If it
enough
is defined
to as
2
With
the
use
equation
of the
(4-21)
definitions
reduces
V22+ V12 V_ 2
of D,
(eq.
(4-21
(4-12))
and
R
(eq.
(4-15)),
to D=D,-R
As seen
from
equation
(4-22)
(4-13), _ =_D_
Substitution
)
of equations
(4-23)
and
(4-23) (4-14)
into
equation
(4-22)
then
yields 2
COS
_2
.
D -
sm Aa--R _z_
This
relation
reaction
is like
and
Attempts overall
(ref.
loss
different not
4)
with
give the
figure
4-4(a).
been and
made
compressors,
with
diffusion of reaction
same first
to correlate
suction-surface
of increasing correlation
values
Consider
for
(4-24)
_1
the
two
terms
blade
loss
involving
solidity. have
definite trend but complete blade
that
COS
turbine
(ref.
5)
diffusion
loss with could not
increasing diffusion be obtained. Such
parameter
alone
and
solidity
would giving
not the
with
parameters.
both A
was established, a correlation of be expected,
same
value
since of D do
loss. the
effect
As reaction
of reaction
on loss,
is reduced
from
as shown
a relatively
qualitatively high
value
in near 111
TURBINE unity,
DESIGN AND APPLICATION
there
reaction tion
occurs
to negative
in loss varies
regime, of the
frictional on the
other
the increased these
are
desired
in many
surface
opposing
the
in chapter
applications,
per
the
solidity.
loss per
unit
surface
diffusion
required. The
value
is used.
4-4(b).
increases,
loss occurs
o .-I
(b)
Axialsolidity,ox
112
the
is increasing suction-surface
and solidity.
of the because
A minimum
As solidity
Reaction,R
FIGURE 4-4.--Loss
varia-
reaction
blading
A minimum
(a) Reaction. (b) Solidity. trend with reaction
nature
negative avoided
area
of the
as the
is usually
As solidity is increasing.
This
in
in boundary-layer
The
in figure
flow
factors.
6)
conventional
unit
reductions
rapidly.
change
to diffusing.
when
optimum
hand,
by
on loss is indicated
area
loss. Further
loss to increase
discussed
accelerating
at some surface
the
highly
of solidity
in blade
is caused
loss encountered
effect
loss occurs
of
(which from
high
cause
reaction
although
The
increase
values
with
characteristics flow
a gradual
amount
of
is reduced, because
of
as a result diffusion
BLADE
parameter
corresponding
factors
such
tribution,
to the
as Reynolds
and
rate
not exceeding
number,
of turning.
about
analytical
optimum tion
(4-14),
the
blade-row
locus
experimental
inlet range
of points
In order
_b, is equal
axial
and
solidity
of angles.
The
for impulse
have
velocity
previously,
been
1, minimum
to 0.8. can
exit flow angles,
disvalues
to identify
loss occurs
By using
this
be determined
and
dashed
made
when
value
the
in equa-
as a function
this is plotted
(long-short)
in figure
curve
of
4-5 (a)
represents
the
blading.
to determine
it is necessary
surface
of many
Solidity
attempts
to reference
coefficient optimum
for a wide
of suction as mentioned
of Optimum
According
loading
shape
is a function
2.0 are used.
and
solidity.
Zweifel
solidity
In gencral,
Selection Both
optimum
DESIGN
the
to determine
optimum the
stagger
values
in terms
of actual
angle
as, because
solidity,
_X
_-
(4-25) COS
An analytical to the
blade
flow angles
solidity
were
figure
and
The
determined
with
solidity
is seen
Loss coefficients function
blades
in relative various
exit
solidity
from
the
angle
exit
gets
nounced
and
optimum
the
the
loss
spacing.
cannot be correlation
Thus,
the
optimized is somewhat
obtained blade for each clouded.
any
shape
and
solidity,
a figure
the
such
exit
of selecting
some increase
in loss.
becomes
more
a given resultant and
as solidity
that
the
curves
blade
shape
velocity significance
the
deviation
significant severe
for
of exit angle,
loss region more
for
solidity
importance
loss, and
8 as a
angle coefficients,
against
values
as
efficiency
in reference and
4-7
be recognized by using
4-6.
(al = - a_). These
of minimum
become
was
in figure
maximum
presented
negative)
cause
It must
6 from
in
solidity
efficiency
here
solidity)
indicate
minimum
penalties
value.
4-7 are usually
not the
as shown
7, where
in figure
(more
region
does
smaller,
are
blades
curves
angles,
angle
of actual
an optimum
yielding
of
here
larger
in the
optimum
from
the
flat
the
data
impulse
These For
to that
stagger
values
as shown
in reference
(inverse
replotted
exit
of reference
close
ratio
and
solidities,
on cascade
are
angles.
are rather
of figure
to be quite
optimum
6 compared
data
rotor
(al = 0) and
solidity.
the
6 to relate
Thus,
of inlet
as optimum
based
terms,
optimum curves
with
of pitch/chord
reaction
solidity.
of reference
different
determined
figure 4-5(b) for this case.
in reference
as a function
way
four
used
axial
authors
in this
measured
was
the
obtained
4-5(b).
The
model
as
such
in As pro-
departs as those
and varying distribution of such
a
113
TURBINE
DESIGN
AND
APPLICATION
Inlet-flow
6--
\
\
\
angle,
\
\ \
_4
Typeof
\ -2
_ "" _. _ _ _ _
"_3-
_1_
bladerow
"_
40
-----Impulse -- ---- Decelerating
\ \ \\\\\
\\
g' 1 (a)
o1.1_
I
m
I
I
I
\
\
\ \
% \ deg
\80
\
\
\70
\
\ \
I
Inlet-flow angle,
\ \
I
\
\ \
\
\ \
\
\ \
\
\ X
\ \
\ \
(b)
o -20
FIGURE 4-5.--Effect
114
I -30
I
I
-40 -50 -60 Exit-flowangle,o2, deg
(a) Axial solidity. (b) Actual solidity. of inlet and exit angles on optimum coefficient _= =0.8.
I
I
-70
-80
solidity.
Zweifel loading
BLADE
•9O _
Optimumsolidity from
DESIGN
Number blades
•_
. 88 •
-
o
24
o
of 64
" I 1.2
.86 .8
FmURE 4-6.--Variation
I [ 1.6 2.0 Solidity, o
of efficiency
10,--
with solidity
I 2.8
for four turbines
Reactionblades(ol = O) Impulseblades(al = -a2)
------
\
I 2.4
\
i
_I
6'_
_ .... %
I
""*-
_
Ol
The
are
with
those
that
agreement
not
good
obtained
analytical and
the
solidity time
curves impulse with
is that
mental
results
factors
that
obtained
the
exit-angle do cross
exit
angle
pertain act
3.0
and values. other
blading,
are just results
to one
to determine
angle
the
3.5
shown
for both
optimum
and
blade solidity
It is obvious results
experimental
and
can and
the
in optimum be said
assumptions,
profile,
is
(c_ = 0) blading
variations
All that
in
compared
analytical
the reaction
many
shown
are
4-5(b).
the the
indicated
similar.
involve
particular
and
coeffi(.ient.
results
4-8
in figure
Although the
not
cascade
in figure
experimental
each
analytical
from
exit
analytically
(al = -a_)
the
,,--7o
2.0 2.5 Solidity, o
against
between
for most
"_-40
of solidity and exit angle on blade-loss
solidities plotted
-60
80
1.5
optimum 4-7
_
>"
_
FIGURE 4-7.---Effe(:t
figure
I
__
4
-70
i" _
7.
Exit-flow angle, a2, deg
\ 8--
of reference
the there
in a manner
are that
at
this
experimany we do 115
TURBINE
DESIGN
AND
APPLICATION
Basedon analyticalresultsof fig. 4-_b) Basedon experimental resultsoffig. 4-7
------
Inlet-flow angle, al, deg - 2
-a 2
1-0 E -(]2
o
I
-30
FIGURE
not
yet
are
more
fully
mental
results, ¢,
such
recommended
of
Analytical
used
to
in reference
which
In the
past,
some
the
on the
modification
is suppressed The
to reduced
boundary
layer
increasing
the
the
Certain
Two
are
tandem
the
applying
alternate
blade
in references test
references The
15 and
practice
than
the
0.8
have
boundary-layer to stator
blades
blades
low-solidity
and
are presented tandem
removing
blades
jet-flap
on
marginal
better
potential
in figure as well
4--9. as the
are summarized
of low-solidity
in references
and
or
with
concepts tests
the
of turbulators
illustrated
rotor
Cascade
is one
by blowing,
perhaps,
are
separation
layer explored
treatment
10, respectively.
that
solidities,
include
by use
been have,
separation
lower
of separation
could layer
that
been
such
boundary
boundary
which
plain,
11 to 14. Turbine
rotors
are
presented
in
16, respectively. operates
of suction-surface
diffusion
minated
the
116
the
blades,
blade
at about
4-5,
experi-
occur.
region
treatments
energizing of the
do not
in the
concepts
jet-flap
tandem
Such
})e utilized
blade
concepts
with
layer
has
To achieve
losses
jet-flap
the
9 and
and
results
must
high
concepts
and
design
higher
in solidity blade.
of these
alternate
Studies
tandem,
solidity.
by suction, turbulence
success.
concept
of the boundary
approach
blade.
of the
the associated
treatment
Current
are
Blading
to reductions
surface
in blade
and
4-7.
of figure
than
1.
limitation suction
as those solidity
is slightly
Ultralow-Solidity
occurring
I -80
such
in figure
1.0,
I -10
solidities.
optimum
shown
of 0.9
optimum
results,
to determine
as those
values
I
-50 -_ Exit-flow angle,(]p deg
4-8.--Comparison
understand.
frequently
is to use
I
-40
point
on the principle is utilized of separation.
that,
(perhaps The
2),
although the
remaining
a high value
front
foil is ter-
diffusion
then
Tandemblades
FIGURE
takes
place
on the
20 to 30 percent The trailing the own
lift.
foil with
blading
a clean
mainstream
point
around
In addition,
momentum.
the
the
Figure
edge,
delivers
4-10
layer
through
perhaps
and thc
slot.
a secondary air stream main stream. This jet
trailing
jet
with
concepts.
boundary
air going
jet-flap blade operates with edge perpendicular to the
stagnation
DESIGN
Jet-flapblades
4-9.--Low-solidity
rear
of the
BLADE
thereby
some
shows
force
jetting moves
substantially to the
experimental
blade
velocity
out the the rear increasing
througl_
its
distributions
1.2 (-1 Jeton (4 percentflow) 0 Jetoff .-._- -O..[:r
1.0
_,
Suctionsurface IJ
_e'-
6I I°
4
2
Pressure
FIGURE
f_
I
__ ,
0
surface
I 20
4-10.---Jet-flap
I
I
40 60 Axialchord,percent
experimental
velocity
I
I
80
100
distributions.
117
TURBINE
DESIGN
AND
around
one such
longer
a requirement
APPLICATION
blade
with
to be equal
at the blade
a rectangular
shape,
unity.
Also,
thus
the
for solidity
sidered
only
other
load
on the
tendency
reductions. such
The
loading
coefficient
suction
the
blade
the The
determined This
from
involves
jet
connecting
flap,
to
channel
and
exit must
thc
provide
has
The
stream.
the
concepts
however,
been
reduced,
offer
the
poten-
will probably air
flow
and
the blade and
and
be con-
is required
parts
profiles
flow turning
blade
for
must
be designed.
of the
and
blade
between the
minimum
the
must the
connecting
with
spacing
geometries
transition
surface
the
itself exit
exit
efficient
The
required
selected
inlet
inlet
a smooth,
free
approaching
DESIGN
of the
profiles.
provide
now approaches
closely
is substantially
a secondary
considerations,
determination
surface
designed
is no
surfaces
cooling.
length
solidity
pressure
diagram
tandem-blade
where
as blade
chord
jet on, there
and
_ more
surface
BLADE-PROFILE After
the
to separate.
and
for applications
purposes,
on. With
on the suction
edge.
the
the jet-flap-blade
off and
velocities
trailing
with
diffusion
suppressing
Both tial
the
the jet
for the
be
blade
inlet
and
edge,
the
loss.
Exit Consideration throat,
and
the
Trailing trailing
of the suction
edge.--In edge
blade surface
17, an increase loss.
This
discussion
in chapter
significant
effect
4-11,
which
of the shows
new
exit-velocity
just
within
trailing-edge station The
example diagram
the
blade
blockage
2, which
that
at 2a include
sections
have
region.
in a higher just
been
conservation
beyond used
with
continuity
in
turbine-loss also
has
with
the
2a, which
reduced
velocity
use of figure
area
at station
blade this
trailing-edge
used. due
to the
2a than
(4-26)
_)_
at
region.
"within-the-blade"
momentum:
(p
A
is located
:
or2
a
exit region. nomenclature
of tangential
S COS
118
an increase
of the
the
obtain
smallest in
at station The
edge.
shown
thickness
blade
V,,.2, = V,,,2 and
the As
causes
as part
the
to
trailing
considerations.
will be made
is constructed
results
the
trailing-edge
effect
blade
and
in the
trailing-edge
is located
equations
diagram
addition,
blockage
throat
further
on the flow blockage
Consideration
trailing
thickness
is discussed
7. In
the
it is wise to utilize
mechanical
in trailing-edge
effect
includes the
of turbines,
with
the
section
between
the design
consistent
reference blade
exit
(4-27)
BLADE
DESIGN
Station 1
0
$
FIQU_E 4-11.--Blade
where
t is the
trailing-edge
is determined between
from
stations
are usually
thickness,
equations
2a and
small)
Mach
preceding
at
and
flow 3Iach
blockage
can cause
station
design
whether flow rate
Throat.--Since,
the
throat
design
assumes
no
change
inside a turbine
use of the
up to the throat, One
also
number
high
in general, o (see
fig. 4-11)
technique
flow
(since
at the
blade
conditions
region,
used
area, a rather
successfully velocity and
exit
a straight
the large
(station
2)
trailing-edge important
will occur
row operates
or minimum becomes
from
as is often the
an
as at station
It is, therefore, row
flow
changes
to have
angle
angle
asa
the the
be designed
the
blade
blade
flow angle
assuming
determined
choked. the
The
be
subsonic
"inside-the-trailing-edge" in
by
must
Because
be obtained.
procedure.
can
2a to become
choking
opening
sion makes
blade
cannot
the flow accelerating of the
in the
(4-27)
incompressible
2a
the
to be
the
station assumptions.
specified
or feet.
a velocity-diagram
and
is often
to determine
and
The
to produce
number
(65 ° or greater)
(4-26)
or isentropic.
equations
in meters
2 to bc either
exit angle of a2a in order 2 outside the blade row. The
section and nomenclature.
such
that
as a nozzle,
with
the determination critical
aspect
to give this diagram. suction
of
dimenIf one surface 119
TURBINE
DESIGN
between
the
obtained
from
AND
APPLICATION
throat
and
the
station
velocity
2a,
then
diagram
the
throat
at station
dimension
2a by
using
can
the
be
following
equation:
o( =
where
o is the
throat
If it is assumed throat
and
the
1
opening, that
cos a:_ 8
cos
in meters
the
velocity
"free-stream"
(4-28)
(T2a
or feet.
and
station
loss do not
change
between
the
2, then
0 -= 8
When the
this
method
angle
(4-28)
of the
and
solidities
(4-29)
applies
flow the
sonic
exit.
For
exit
(throat) perhaps, achieved additional the
case
predicted at exit
blade
condition
at the
flow
back
the
channel
occurs
channel
exit
downstream dimension
condition
i\[ach
o would
then
for expansion choking
such that
from
(4-28)
velocity,
1.3, the
low supersonic
the
be
across
flow is subsonic.
to account
supersonic
about
could
occur
at the section
a convergent-
numbers
been found that satisfactory performance is still located at the exit of the channel,
expansion
required
For
to the than
within
exit
This 60 ° and
equation
to a supersonic
be modified
throat
would
from
blade-row
than
deviation
that
(cqs.
8 compares (4-29).
greater
determined
changes
methods
by equation angles
to 35 ° . This
expands
greater
Both Reference
gradients
the
must
is obtained.
1.3), it has if the throat
as
row
numbers
be located
passage
down
wherc
dimension
5[ach
must
divergent
the
throat
from
following
those
thickness
its length.
dimensions.
agreement
dimension to the
within
this computed
not
as well as larger
throat-opening
If the
but
with
close
(4-29)
of trailing-edge
throat
of up to 5 ° for exit angles
due to lower the throat. The
angles
q2
effect
position
indicates
deviations
the
give similar
exit-flow
comparison
case,
throat
(4-29))
measured
or
is used,
COS
throat.
be computed
(up
to,
can be and the In by
this the
equation:
(4-30) o = o_ \A _} where
058
throat
opening
supersonic
computed velocity,
Act
flow area
for sonic
A,,
flow area
for supersonic
120
flow,
from
equation
m; ft m2; ft 2 flow,
me; fC"
(4-28)
or
(4-29)
for
BLADE
DESIGN
1.0
¢3
.9--
1
Rt
I
1.1 Mach
FIGUttE 4-12.--Variati(m
This
area
exit,
correction,
is shown
Suction surface
surface
be made edge
the
from
throat
such
region,
assumed
isentropic
from
throat.--The
and
trailing
considerations
5[ach
suction-surface
number
flow Mach munl_er.
flow between
throat
and
4-12.
downstream
between
1
1.4
ill flow area with supersonic
with
in figure
I
number
diffusion
on the
as structural
level (D_),
selection
edge
and
and
in the
losses,
surface
area
type
surface
integrity
associated
blade
of the
suction
of
must
trailing-
desired
level
resulting
of
from
the
design. A "straight unity)
back"
are specified
or transonic the
uses tail
problems solidity ture ably at
this
to the
curw'd
and
ref. 8), if the is small. 5[ach
surface
suction-surface is improved of remaining
and integrity
are
great. 5Iach
regions.
between
the
velocity
distribution.
curvature
region.
This
permits
some
numbers design type
and
it adds
by introducing is used,
t)y figure
(greater
0.8, than
curvatures
trailing throat
edge the
effect
(which
the
curvature
0.8),
the
has an effect
to trailing
is
effect
be lower
selected
velocity
angle of this
4-13
should
of curvature
dif-
consider-
a wedge the
is less than
In general, from
flimsy. of curva-
number
decreases
structurally
low-
amount
blading
and
Principal
preclude
some
As indicated
throat
next
utilizes
blade
The
low.
low D, values
tail of the blade,
Therefore,
number
if the
can become
trailing-edge
(,xit Mach
severe.
edge
subsonic
in the
flow acceleration
losses
the
()f the
High
to prevent
associated
blading
on the
(approximately
discussion
that
loaded
exit-flow
At higher
on loss can become suction
the
on loss is not
effect
higher
and
If eonv(,ntionally
surface
by the
in order
keep
of D,
are permissible.
of surface
h)ading
structural
exit.
edges
long trailing
throat
low values
be indicated
surface
the
when
trailing
gas-turbine
the
from
the
blade
a straight
and additional
the
long
type
conventional
between
fusion
is used
as would
of the
with designs
5lost
and
blading,
paragraph, on
design
in
for the on the
distribution edge
instead
constant. 121
TURBINE
DESIGN
AND
APPLICATION
Mach number 1.0
__o .-
j
m
_\\ L°7
.2 .4 .6 .8 Ratio ofbladespacingto surfaceradiusofcurvature
FIauR_
4-13.--Variation
of
profile
between
h)ss
throat
with and
Math
exit
numl_er
(from
ref.
and
surface
curvature
_).
Inlet The
leading-edge
than
the
exit-region
leading-edge erally
geometry
diffusion
and
numbers,
inlet
the
must blade
for thc
lead
that
inlet.
the
.\lach
through
the
blade
blading
area
With
5[aeh
arc
usually
lead5 [ach high
high
inlet
5[ach
is not so severe
and
to det('rmin('
and
The high
of suction-surface
contraction (4-26)
row.
is gen-
excessively
values
losses.
large
number and
binding,
to high
Equations
can also be used
a relatively
the
i:_creased
flow angle
circular
could
edges
can
limit
leading the
region. result
pressure-surface ellipses,
(4-27),
which
as
were
a blade-inlet
opening
to check
for blade-
number
freedom The
of
velocity
peaks
leading
edge.
permit
of the
variations or eliminate
the
leading-
remaining
and
is t:o join
the velocity
them
with
is arbitrary
selection
associated
in curvature
trailing-edge
this
velocity-distribution
curvatures
Blade-Surface Once
specified,
large
portions
which
edges
in undesirable
be used to minimize
122
inlet,
less critical
choking.
leading-edge
task
blade because
of low-reaction can
be taken exit,
row is usually
for low-reaction
toward
at the
bIade
case
region
"within-the-blade"
Although and
the
inlet
a tendency
care
to choke and
In
in the
increases
concern
blade
the
be used,
and then
a serious
blading.
velocities
At
earl usually
low at the inlet
number
used
geometry.
radius
ing edge bccomes
of a turbine
with
on both Other
around
in
circular the
leading
suction-
geometries, the leading
the
such edge,
and as can
peaks.
Profile geometri('s a profih_ that,
have
been
yields
the
selected, required
the flow
BLADE
turning
and
desigu
a satisfactory
procedure
must
to an accuracy Two
sufficient
of the
major
Velocity
gradients
pressure
surface
turn
the
flow
occur
as a result
of these
factors
influence
The
channel
and
of the
theory
from
Pressure
_ Suction
surface7
_su rface
The rows
in the
figure
difference and,
considerations.
serves
to
the
required
to
therefore, Since
distribution,
as the basis
available
4-14.
suction
position
velocity
limits).
both
the design
of a quasi-three-dimensional
that
ncxt
blade.
the blade diffusion
illustrated
channel
programs
in the
(e.g.,
static-pressure
least
the
through
in streamlinc
be at
computer
are discussed
arc
the
of radial-equilibrium
should the
around
controls
the blade-surface
flow analysis
procedures putations
across
variations
velocity
used
design
considerations
occur
Radial
distribution
the flow conditions
to impose
as a result
flow.
procedures
velocity
describe
DESIGN
nature.
for these
to perform
the
design com-
chapter.
..-Pressure surface
Suction surface_..
Cross-channel
distance
(a)
__
, 'lEi.:_.i:!_._.:._::..::::::_i_!| Tip : _i_ Rotorf_ii!i|
-'Nl ,
"'- Tip
_
_I
°--
NN
¢";1
,-Hub
_:: /
Velocity (b)
(a)
Cross-channel (b)
FIGURE
4-14.--Turbine
Radial
variation. variation.
blade-row
velocity
variations.
123
TURBINE
DESIGN
AND
APPLICATION
REFERENCES 1.
O.:
ZWEIFEL,
Angular 2.
LIEBLEIN, sion
The
STEWART,
Blade
Paper
Effective
RM
E56B29, Y.;
for
a Series
Four 6.
HELLER,
E56F21, A.;
Investigation
8.
AINLEY,
l).
G.;
BETTNER,
RM
Loaded
10.
H.
cepts
Designed
2, Apr. 11.
STABE,
ROY
NOSEK, tion
13.
NOSEK,
STABS,
U.;
AND
Gt.
E55BOS,
of
Turbine-Blade-
WARREN
WHITNEY,
by
Parameter
Cascade
and
for
1955.
Changes
in
J.:
Blade
RICHARD
Turbine
at
R.:
An
Analysis
Geometry.
H.:
Experimental
Four
Rotor-Blade
Examination
of
Turbines.
Rep.
Axial-Flow Britain,
the
Flow
R&M
and 2891,
1955. M.
:
Summary
of Tests
in Three-Dimensional
R.
J.:
Turbine
Some
on
Cascade
Experimental
Blade
Two
Highly
Sector.
Paper
Results
Loading.
J. Eng.
Ratio
Cascade
to Spacing
KLINE,
JOHN
Blade
Blade. and
with
Two-Dimensional Chord
of Two
Power,
NASA
JOHN NASA
of 0.5.
F.:
Chord
of
TM
vol.
Con92,
Turbine
no.
X-1836,
X-2183,
Stator
X-1991,
Cascade TM
1970. Investiga-
1969.
Two-l)imensional
TM
Two-Dimensional of Axial
Test
NASA
F.:Two-Dimensional
Design.
AND KLINE,
Rotor
l)_ign
Blade
of
1969.
and
Tandem M.;
ROY G.:
Use
Losses.
Diffusion
Two-Dimensional
AND
STANLEY
Nov.
of Axial
Turbine
Stator
C.
of
Concepts
])esign
Ratio
STANLEY
W.:
198-206.
of a Turbine
Jet-Flap 14.
pp.
STANLEY
JAMES
Rotor-Blade
with
AND CAVlCCHI,
G.
AND ROELKE,
G.:
with
Ex-
Diffusion
1952.
Rows
to Increase
1970,
Blade 12.
G.;
R.:
Using
Correlation
Designed
NOSEK,
ASME,
LUEDZRS,
L.;
L.;
Council,
Blade
69-WA/GT-5,
ROSE
Blade
; AND
Turbine
in
Affected
MATHIESON,
in
L.
L.:
RM
WARNER
E52C17,
Research
JAMES
MICHAEL
MISER,
Turbine
Thickness
NACA
Conservatively
AND
Aeronautical 9.
a
Losses
Diffu-
1956.
NACA
Pressure
AND
])escribing
Blades
Losses
WHITNEY,
of
Solidities.
L.:
in Axial-Flow-
1967.
J.;
WARNER
Rotors.
Viscous
RM
Large
436-444.
1953.
AND VANCO,
Nov.
Momentum
Turbine
STEWART,
JACK
pp.
ROBERT
Loadings
Characteristics
ASME,
on Wake
Turbine W.;
with
1945,
1956.
of Subsonic
JAMES
J.;
WARREN
AND STEWART,
Turbomachine
NACA 7.
Blade-Lolling
in
Blade
E531)O1,
Turbine
WHITNEY,
Based
Transonic
MISER,
of
Losses
RM
Especially 12, Dec.
AND BEODERICK,
ARTHUR
Thickness
ROBERT
Element
NACA
32, no.
Limiting
GLASSMAN,
Momentum
NACA WosG,
L.;
C.;
and
67-WA/GT-8,
WARNER
vol.
FRANCIS
Elements. L.;
Blading,
Rev.,
Losses
of Axial-Flow
Parameters.
5.
SCHWENK,
WARNER
STEWART,
Turbo-Machine
Boveri
for Estimating
amination
4.
of
Brown
SEYMOUR;
Factor
Compressor 3.
Spacing
Deflection.
Cascade
Test
of a
1971.
Cascade
Test
to Spacing
of a Jet-Flap
of 0.5.
NASA
TM
Turbine X-2426,
1971. 15.
16.
BETTNER,
JA_ES
Solidity
Tandem
BETTNER,
JAMES
Solidity, 17.
PRUST,
Jet
ing.
124
NASA
and TN
l)esign Rotor.
L.:
Flap
HERMAN
Geometry
L.:
l)esign Rotor.
W.,
Jm;
and
Experimental
NASA and
on
1)-6637.
1972.
Results
CR-1968,
AND the
HELON,
of a Highly
Loaded,
Low
of a Highly
Loaded,
Low
1971.
Experimental
NASA
Thickness
Results
CR-1803,
1972. RONALD
Performance
M.:
of Certain
Effect
of
Turbine
Trailing-Edge Stator
Bind-
BLADE
DESIGN
SYMBOLS A
flow area,
C
chord,
D
diffusion
F
force, N; lb conversion constant,
g K
ratio
m_; ft 2
m; ft parameter
of inlet
o
throat
P R
absolute reaction
8
blade
t
trailing-edge
V
absolute
X
axial
o_8
1; 32.17
to exit tangential
opening,
(Ibm)
(ft)/(lbf)
components
(sec 2) of velocity
m; ft
pressure, spacing,
N/m2;
lb/ft
_
m; ft thickness,
velocity,
distance,
m; ft
m/sec;
ft/scc
m; ft
fluid absolute
angle
from
axial
direction,
deg
blade
angle
from
axial direction,
deg
stagger
ratio of specific heat constant volume density,
( V_ ._/V,._)
kg/m'_;
lb/ft
at
constant
pressure
to specific
heat
at
a
solidity
_bz
loading
coefficient
defined
by equation
(4-6)
loading
coefficient
defined
by equation
(4-5)
Subscripts" cr
critical
inc max
incompressible maximum value
rain
minimum
opt
optimum
p s
pressure suction
ss u
supersonic tangential
x 1
axial component blade row inlet
2
blade
2a
within
value
surface surface
row
component
exit
trailing
edge
of blade
row
Superscript" '
absolute
total
state
125
CHAPTER 5
Channel FlowAnalysis ByTheodore Katsanis
The
design
of a proper
blade
profile,
chapter
4, requires
calculation
determine analysis
the velocities on the blade theory for several methods
of the
discusses associated computer Lewis Research Center. The
actual
cannot
velocity
be calculated viscous,
passages.
To calculate
simplifying simplified surfaces Similar mean
distribution
surfaces. This used for this
to flow
on or through
hub-to-shroud shown
directly,
but
stream in figure
provides
surface
extreme
to
at
the also
NASA
flow
field
complexity
geometrically therefore,
two-dimensional
of
complex certain
three-dimensional
5-1 (a),
(commonly
does
information
There
are
tribution
two
over
formulation
one
of the
mathematical we
velocity-gradient
parts
will
to a method
of these
flow
surfaces.
and
problem. discuss
the For
stream-
(stream-filament)
yield
The second
is
Such
and
is the
is the
mathematical The
surface which
yield
a velocity
dis-
mathematical
numerical
solution
formulation
potential-function
methods.
velocities
solutions,
part
part
meridional
blade-to-blade
to obtain
first
the
blade-surface
5-1 (c))
of analysis
the
called
for the
(fig.
surfaces.
problem,
not
required
(fig. 5-1 (b)) and orthogonal surface the desired blade-surface velocities.
problem,
in order
are illustrated in figure 5-1 for the case of a radial-inflow turbine. surfaces are used for an axial-flo(v turbine. A flow solution on the
surface),
of the
The
various
of
developed
distribution,
made.
field
section
a blade-row
of the
velocity be
last
chapter presents calculation and
were
flow through
a theoretical must
that
because
three-dimensional
assumptions
flow
throughout
time
in the
blade-row
programs
at this
nonsteady,
as indicated
stream-
of the
methods and
and
potential-
TURBINE
DESIGN
AND
APPLICATION
Blade-_,-blade
Hub-to-shroud stream surface
-_ |
surface] I
(a)
0_)
,- Ortho_nm
(c) (a) Hub-to-shroud
stream surface. (b) Blade-to-blade (c) Orthogonal surface across flow passage. FIOURE 5--1.--Surfaces used for velocity-distribution calculations.
128
surface.
CHANNEL
function
methods
will be described
solution.
A similar
type
The
of analysis
velocity-gradient
for solutions The
equation
on any of the
following
of analysis (1)
The
surface
flow
Thus,
if the
fixed
coordinate
(2)
The
blade-to-blade
surface
for the meridional is general
surface.
and can be used
are
made
in deriving
the
various
This
means
methods
herein:
at any
blade
can be made
ANALYSIS
surfaces.
is steady
velocity
to the
to be presented
assumptions
discussed
relative
FLOW
relative
given
point
is rotating,
the
to
the
blade.
on the blade flow
would
does not
not
that
vary
be steady
the
with
time.
relative
to a
system.
fluid obeys
the
ideal-gas
law
p=pRT
(5-1)
where p
absolute
pressure,
p
density,
kg/m_;
R
gas constant,
T
absolute
The
lb/ft
lb/ft
2
S
J/(kg)
(K);
temperature,
or is incompressible (3)
N/m_;
(ft) (lbf)/(lbm)
K; °R
(p = constant).
fluid is nonviscous.
A nonviscous
The blade-surface velocity is calculated, extends to the blade surface. (4)
The
fluid
(5)
The
flow is isentropic.
(6) inlet.
The
total
(7)
For
the
assumption
has
a constant
heat
temperature stream-
is made
and
and
that
Y is the
absolute
do
particles
total
vector.
not
change
their
absolute
change.
For
example,
particle
at
times
t and
t-t-At.
particle
changes
blade,
rotation the
is zero. particle
has rotated,
In
and
Of course,
layer.
free
stream
are
uniform
analyses,
across
the
irrotational.
the
shape
additional
because
(5-2)
Intuitively,
orientation figure
this with
5-2
means
time,
shows
absolute
frame instant
of time,
of reference
relative
the
frame
that
although
a hypothetical
at a later
in a frame
the
Therefore,
Y = VX V =0
may
net
no boundary as if the
pressure
flow is absolutely
velocity
its location
has
capacity.
shape
their
fluid therefore,
potential-function
the
curl where
(°R)
of reference,
of reference
the
but
the
to the
has rotated.
129
TURBINE
DESIGN
AND
APPLICATION
Direction of rotation
Time = t
r-l LJ
Time-t+At
I
I
(Absolute frame of reference)
Time=t + At (Relativeframe ofreference)
FIGURE
Some also
numerical
techniques
be discussed.
techniques excellent given
However,
for solving theoretical
in Chapter
STREAM-
5--2.--Absolutely
irrotational
for solving it must
the
simplest cascade 130
stream
IV of reference
AND
be emphasized
equations
that
there
can
be
of streamlines.
in figure
5-3.
only
will
are many a few. cascades
An is
1.
POTENTIAL-FUNCTION
function
is in terms as shown
mathematical
these equations, and we will discuss discussion of flow in two-dimensional
Stream-Function The
flow.
ANALYSES
Method
defined
several
Suppose
It is assumed
ways,
but
we consider that
there
two
perhaps blades
is two-dimensional
the of a
CHANNEL
FLOW
ANALYSIS
1 .8 Mass
.6
flow fractbn
.4
0
\\\\
FIGURE
axial
flow here,
5-3.--Streamlines
so that
the
there is no variation of the rotation about the centerline. Shown the
in figure
blades
passing line.
Thus,
the lower streamlines
the
radius
r from
flow
in the
5-3 are a number
is w. The
between
for a stator
number
the upper upper
surface have
surface
centerline
radial
streamline
of the lower
(which
The
is a streamline)
It will be recalled
There
mass
indicates blade
and has
and
may
be
flow between
the fraction the given the value
of w
stream0, and
of the upper blade has the value of 1, while the remaining values between 0 and 1. Note that a value can be asso-
ciated with any point in the passage. This value function value and can be used to define the stream (or uniform)
is constant
direction.
of streamlines.
by each surface
the
cascade.
that
mass
flow can be calculated
is called function.
the
stream-
for a one-dimensional
flow by w= pVA
(5-3) 131
TURBINE
DESIGN
AND
APPLICATION
where W
rate of mass
V
fluid absolute
A
flow area
This
flow,
kg/sec;
velocity,
normal
can be extended
lb/sec m/sec;
to the
ft/sec
direction
to a varying
of the velocity
flow by using
V, m2; ft _
an integral
expression:
w= f a pV dA Since
this stream-function
cascades relative
(blade velocity
analysis
rows),
the
W, which
velocity V. We will assume the mass flow wl._ between fig. 5-4)
can be calculated
fluid
applies velocity
(5-4) to both will
be
stationary
and
expressed
in terms
reduces
blade
to absolute
that any
has a uniform height b. Then, QI and Q2 in the passage (see
by QI
wl._ --/Q
132
5-4.--Arbitrary
(5-5)
_ pW,,b dq
-'_Q1
FIGURE
of
for a stationary our cascade two points
row
rotating
•
curve
joining
two
points
in
flow
passage.
CHANNEL
where
Wn is the
hand
normal
relative
of the line going
that
wl.t will be negative
The
integral
dependent With
velocity
is a line of path
from
for steady
function
in the direction
QI to Qt. This
if Qs is below integral
the use of equation
for the stream
component
the
flow relative (5-5),
points
of the right-
passing
means
through
Q_ and
Q2 and
Q1. is in-
to the cascade.
an analytical
u at a point
ANALYSIS
sign convention
a streamline
between
FLOW
expression
can be written
(x, y) :
/Q(_'Y) pWnb dq o
u(x,
(5-6)
y) = W
where integral in figure Since tively calculate is still
Qo is any
point
on the
is taken
along
any curve
upper
surface
between
of the
Qo and
lower
(x, y).
blade, This
and
the
is indicated
5--5. the
easy
integral
in equation
to calculate Ou/Ox
at the
the
partial
point
in the flow passage,
(5-6)
derivatives
(x, y).
as shown
Let
of path,
of u. For
Xo<X such
in figure
/c_ pWnb u(x,
is independent
5-6.
that
it is rela-
example, the
we will
point
(x0, y)
Then
dq-}- fc ffipW_b
dq (5-7)
y) W
FIGURE
5-5.--Curve
joining
(x,y)
with
a point
on the
upper
surface
of the lower
blade.
133
TURBINE
DESIGN
AND
APPLICATION
(Xo.Y)ff c2 (x,y}
FIGURE 5--6.--Curve
joining
where
C_ is an arbi'_rary
zontal
line
depend
between
on x. Along
horizontal line through (x,y) surface of the lower blade.
curve
(Xo, y)
between
and
Qo and
(x, y).
C2, we have
The
W, = -W_
Ou (x, y) = --
a point
on the upper
(x0, y),
and
C2 is a hori-
integral and
pW_b o
Ox
with
along
C_ does
not
dq = dx. Hence,
(5-8)
dx
w
or
In a similar
manner,
Ou
aW,,b
Ox
w
we can calculate Ou_ Oy
Now From
we will make the
definition
curlV=fOV.
wherei, 134
j, and
\or
(5-9)
use of the fact of the
curl
OV=_ i
k are the
unit
pW_b w that
operator [OV=
vectors
the and
OV._
in the
(5-10)
flow is absolutely the
above
irrotational.
assumption,
+(OV_
OV,_'_k=O
(5-11)
x, y, and
z directions,
respec-
\ox
ov/
CHANNEL
tively,
and
m/sec
Vx,
V_, and
or ft/sec)
considering
in the
V,
are
the
x, y, and
two-dimensional
absolute
FLOW
velocity
z directions,
ANALYSIS
components
respectively.
Since
(in we are
flow only, V.=O
(5-12)
and OVa_ Oz Hence,
equation
(5-11)
requires
OV:,=O Oz
(5-13)
only that OV_
OVx
Ox
Oy
(5-14)
Since V_= W_
(5-15)
Vu-- W_+_r
(5-16)
and
where
_ is the
equation
Actually, in this
angular
(5-14)
the
speed
(in
can be expressed
case.
Now,
and
in terms
of relative
OW3,
OW_
Ox
Oy
flow is irrotational
particular
rad/sec)
with
from
radius
r is constant,
velocities
as
(5-17)
respect
equations w
the
to the (5-10)
moving and
coordinates
(5.9),
0_t
W_ -
(5.18) pb cOy w Ou
= Substituting
equations
(5-18)
and
0 (1 0u\ cox; since
w and
b are both
For incompressible
(5.19)
pb Ox (5-19)
into
; oy/
0 (10u_=
equation
(_-17)
0
yields
(5-20)
constant. flow,
p is constant, 0_U
and 02U
(5-91) which
is Laplace's
equation.
called
a harmonic
function.
Any There
function
satisfying
is a great
deal
Laplace's of theory
equation
is
concerning 135
TURBINE
DESIGN
harmonic
functions
complex
AND
that
important
thing
number
of functions
solution
that
equation
specifying
two
the
The
entire
first
in every figure
5-8.
and
function boundary along
that
HG, HG
satisfy
of analytic
we along
functions
that
the
angle
we can
ABCDEFGHA. CD,
and FE,
AH
part
will (2)
be
a
to either by
condition
Since
region
far
upstream
_0,_ is known. BC,
u--0;
where
than
that
flow
From
boundary
the
distance
flow
way
the
AB and CD.
cascade.
stream entire of u Along
direction
x
infinite
along
value
Wx
5-7.--Two-dimensional
the
u= 1. Along
is, the in the
in
angle
on the
FG,
that
it is along
_ is the
so that the
conditions
exists;
same
as shown
is uniform
and along
condition
1 greater
and the
A typical
the flow is the
solution
boundary that
region.
yl
FIGUI_E
find
determined
a boundary
solution
is sufficiently
specify
Along
is known,
5-7.
a finite
of the
a periodic
and FE is exactly
is the
in figure
it is assumed
flow
we must
region.
be specified consider
Similarly,
AH and DE, Ou/O_ the outer normal.
136
of
a tremendous
The solution
(5-20) and
are and
conditions.
region,
is shown can
there
(5-21),
equation
of the
this
defined,
equation
a finite
must
cascade
is that
boundary or
(1)
It is assumed
was
know
certain
that
passage,
is known.
AB,
here
boundary
thing
is uniform
DE,
to
(5-21)
things:
two-dimensional
/_
to the theory
that
satisfies
Laplace's
flow
is related
variables.
The
along
APPLICATION
of
CHANNELFLOWANALYSIS
H
6/
"_'. E
Uniform flow
Uniform flow
n
L A
y
W
B P
_-_x
_ C FIGURE
Consider
the
differential
5-8.--Finite
solution
of u in the direction
du = OxO'-u dx+_ The
differential
streamline, Along
is 0 because
and
the
region.
velocity
the
of the velocity
W:
dy -- 0
stream
(5-22)
function
vector
must
Ou
8u
Or -
8x
be
is constant
tangent
to
along
a
a streamline.
AH,
and substitution
from
equation
(5-22)
(5-23)
yields
Ou_ 07
Ou dy Oy dx
(5-24)
du -"-dx
tan _
(5-25)
However,
Further, uniform
Ou/Oy there.
is constant
along
AH,
since
it is assumed
(5-25)
s is the and
the
flow is
Therefore, Ou [u(H)-u(A)'] .... 8y s
where
that
blade
(5-26)
spacing in equation
in the (5-24)
1
(5-26)
s
y direction. gives
along
Substituting
equations
AH
(5-27) ia
8
137
TURBINE
DESIGN
Similarly,
AND
along
DE,
APPLICATION
one can calculate
o,,, = We now have
a boundary
condition
shown
in figure
5-8.
unique
solution
to Laplace's
(5-20)),
a unique
subsonic
throughout
There After
This
problem
is always
can
for solving
will be discussed velocity
as the later.
If lines
by
The
as the stream
determine flow
flow
a (eq.
is strictly
differentiation
indirect,
function,
If the potential function be defined so that
¢ exists
blade
surface
stream
of solving
problem and
distribution.
a
potential
is to
from
this
This
will
drawn,
they
function
properties
(i.e.,
can
be
will be orthogonal
will not be defined
but the main
of the
A method
Method
are
function
or (5-21). and velocities
or inverse,
this velocity
flow,
potential
potential
(5-20)
velocities
problem.
on the
will give
irrotational
of equal
The
if the
equation
direct
distribution that
two-dimensional
streamlines.
of the region
compressible
blade-surface
Potential-Function
defined.
For
determined
be obtained
is known
determine a blade shape not be discussed here.
For
boundary will always
(5-21).
is obtained,
passage
a desired
the entire
conditions
equation
techniques
is what
(5-28)
region.
function
the
function. specify
the
along
boundary
solution
are numerous
the stream
throughout this
These
s
in the
and relations
same
to detail
will be given.
the flow is irrotational),
then
it can
-- = Vx Ox
(5-29)
- Vv
(5-30)
and
Oy We will refer tional
relative
assumption system for pure
to absolute to
the
of absolute
does not rotate. axial
flow,
since
velocities coordinate irrotational This the
here,
since
system flow,
does not exclude rotation
we must
have
This,
coupled
used.
implies
the
continuity
relationship
for steady
o(pvx) +o(pv,) =o Ox 138
Oy
the
with
if there respect
the
coordinate
use of the potential
has no effect
radius; that is, the flow is actually irrotational with as we saw in the discussion of the stream function. From
that
flow irrota-
function
is no change to the
blades,
flow, (5-31)
in
CHANNEL
Substituting
equations
(5-29)
and
(5-30)
FLOW
in equation
ANALYSIS
(5-31)
yields
0(oo,o() If the
flow is incompressible,
p is constant, a_
and
a2_
=0 So,
the
potential
pressible,
irrotational
function
satisfy
difference We
function flow,
the
same
lies in the
can consider
specify BC and
Laplace's
both
the
stream
differential
boundary the
boundary
satisfies
same
equation
(5-33) equation.
Thus,
function
and
(Laplace's
for incom-
the
potential
equation).
The
conditions. solution
conditions
over
region
the
entire
shown
in figure
boundary
5-8.
as follows:
We can Along
FG, -
V, = 0
(5-34)
0_ where
V, is the
velocity
normal
to the blade
surface.
Along
AH, (5-35)
and
along
DE,
oue
The
inlet
and
outlet
axial
velocities
are given
by the
equations
W
(v_) ,. -
(5-37)
p_nbs
and W
(V_) o_t-
Along
AB,
uniform
GH,
along
CD,
and
EF,
a periodic
(5-38)
po_tbs condition
exists.
Since
the flow is
AH,
(0yy_),.,=
[_(H)-
_(A)Is
- (V_) _,
(5-39)
Substituting V_ = V: tan/_
(5-40) 139
TURBINE
into
DESIGN
equation
AND
APPLICATION
(5-39)
yields _(H)
Because than
of the
along
=¢(A)q-s(Vx)_,
periodicity,
AB.
¢ is exactly
Similarly,
at the
O(E) Equation This
(5-42)
gives
completes
The
boundary
but
only
the
+s(Vx)o,,,
difference
boundary
point,
_,
greater
along
HG
these
the
lines
for equation
do not
FE
and
(5-32)
determine
additive
boundary
(5-33)
(5-42)
#o_,
in ¢ along
an arbitrary
to equation
tan
tan
conditions
however,
within
at one
solution
s(Vz)_,_
(5-41)
_,,
outlet,
= ¢(D)
conditions,
a solution
¢ is specified unique
the
tan
a unique
constant.
solution,
If the
conditions
for incompressible
CD.
or (5-33). value
of
will determine flow,
a
or to equation
(5-32), for strictly subsonic compressible As for the stream function, there are
flow throughout the region. numerous methods for solving
equation
preceding
ary the
(5-32)
or (5-33)
subject
conditions. A method velocity distribution
references
2 and
to the
for solving to determine
of Stream-
choice (the flow)
of the
three
is not
of stream
function
The
existence
of the
equation. For a line between
the flow be either
tion
is necessary flow was
relative
This of
blade
could function
can easily mass
may
be
function
flow
or steady.
irrotational, the
restricted
is proven
flow to be unique.
for
or incomas to the
function.
incompressible
for the
absolutely
to the
assumptions the stream
we
irrotational,
the stream function to be defined, two points must be independent
that the
(steady,
then
or potential stream
there is little to function. In this
of ease of solution for the boundary is the same: Laplace's equation).
assumptions
applicable,
choice
Method
and incompressible, and the potential
is made on the basis differential equation
if any
pressible
problem of specifying shape is described in
or Potential-Function
If the flow is steady, irrotational, choose between the stream function
However,
the inverse the blade
bound-
3.
Choice
case, the conditions
or equivalent
used
turned
case
the
the mass of path. Some
We
which
axial-flow
from
continuity
flow This
crossing requires
additional the
out
assump-
assumption
that
to be irrotational
considered.
However,
other
be made for other problems. Another restriction is that it can be defined only for two-dimensional
be seen
since
between
two
the stream points,
function and
this
is defined
on flow.
as a percentage
is meaningless
in
three
dimensions. The
existence
irrotational 140
of the
relative
potential
to the
given
function coordinate
can
be shown system.
This
if the
flow
is necessary
is
CHANNEL
because
we must
have
equality
of mixed
second
FL_OW
partial
ANALYSIS
derivatives;
that
is, if 02_
02& (5--43)
m
OxOy
OyOx
then
0 V ----_ Ox _-Oy and
the
flow
must
be
dimensional
flow;
that
irrotational
with
respect
an
assumption
done
is, the
must
by using
the
irrotational.
continuity
Finite-Difference As
stated
posed
by
detail
flow.
rate
In this case,
region
first
step
shown at
typical 5-10. points
The
mesh
point
point
hi, and
in figure tively.
each
5-10. With
equation
mesh
points.
When
this
2ul h_(h_Th2)
finite
is done,
the
2u_ 4-h2(h_+h2)
can
be
can
grid
stream
neighboring
mesh
is labeled
series
distance
following 2Uo]
of this
[
but
2U3
to the
bound-
The
method
with
a lower
points
in figure (eq.
5-9.
(5-21))
function
in the Then
a
can be
is unknown.
points
is shown
the
four
between
A
in figure
neighboring
points
0 to 4 are labeled
expression
for the
irrotational
are h2, h3, and
expansion
be approximated
explanation
problem
of mesh
0, and
distances
of u at points
consider
solution.
equation
The
problems
We will
similar,
is shown
the other
various
function.
grid the
Method
subject
to Laplace's
1 to 4, as shown.
(5-21)
equation
is quite
where
four
similarly,
(Further
Finally,
This
incompressible,
on the stream
A typical
point
value
flow is
used.
of the direct
difference
in consideration
The
being
theory.
a rectangular
the use of a Taylor
tions,
Laplace's
function
5-8.
with
in three-
if the
solution.
of solving
solution
solve
for the
are labeled
denoted
ways
case of steady,
approximation
mesh
only
Stream-Function
in the section
potential
in figure
system a unique
for many
is to establish
finite-difference written
are
we must
for the
exists
exists
or potential-function
discussed
of convergence
The
there
for the simplest
ary conditions of solution
coordinate
the finite-difference
function
function
to assure
Solution
before,
situation
equation.
stream-function
in further stream
potential
made
(5-44)
A similar
to the
be
V.
1 and
0 is
h4 as indicated u0 to u4, respec-
for u in the x- and y-direcby
using
is given
only
values
in ch.
of u at
6 of ref.
4.)
is obtained: 2U4
+h_(h_+h4)
2Uo ] _j=O (5-45) 141
TURBINE
DESIGN
AND
APPLICATION
N I ] Ii-'_ "_ _- .."
. !
_
"
!
\
1
li, ii ¸ I I
_i
fl II, IJ.-"_
--'-..I
[I \_, i\ I .
N
_
ilII i, I
1
_\! " '
1
"
!
i
;
I
r A-
•
_
e
1
,l
"F
'_\{
j
E Jl
il ,II II
i
: !
.,
Ill LI] Lil
!
\\ :
I
I
I
I)
FIGURE
5-9.--Mesh
used
for
a finite_lifference
solution.
h2
h3
0
D
h4
,4
1
FIGURE 5-10.--Notation
142
for adjacent
mesh points and mesh spaces.
CHANNEL
Solving
equation
(5-45)
for u0 yields
the
FLOW
ANALYSIS
expression
4 UO=
E i-1
aiui
(5--46)
where h 3+ h4 al= a0h--_
(5-47)
h3--_- h4
= --
(5-48)
aoh_
hi+h2 a3 --
(5-49)
aoh3
hl+h_ a4 -
(5--50)
aoh4
1 1 ao=(h3Th4)(_T_)+(h.+h,)(_+-_,)
Equation
(5-46)
boring
points
used.
At other
but
the
these
points
boundary
points.
Ou/O_
holds
along
can be used along
by equation
if point
the
the
periodic
boundary
that
1 in the
of the
neigh-
point
can be
(5-46)
to obtain
alternate
boundary
cannot AH
0 is on line AH,
be used,
equations
at
in figure
5-9,
then,
a finite
gives
(5-52)
(tan-Bin)
0 is on line DE,
along
boundary between
it is known point
points
If one
of u at that
equation
If point
Uo= u3-
For
point.
value
the upstream
(5-27).
Uo= u4+h4 Similarly,
the
the boundary,
conditions
approximation
mesh
then
1 (5-51)
interior
surface,
For example,
is given
difference
at every
is on a blade
1
AB
CD,
condition.
A and ul=ul.s-1, y-direction,
and
h3 (tans-_°"'
If
B, the point where as shown
(5-53)
)
equations
can be derived
the
0
point
I is outside the
point in figure
(fig.
5-11)
the boundary.
by
is on
the
However,
1,s is a distance 5-11.
using
Substituting
s above this
143
TURBINE
DESIGN
AND
APPLICATION
H
2 31
I
G.
I
u2 "u2,-s
A
2,-s
FIGURE 5-11.--Mesh condition
+1
in equation
(5-46)
point on line AB.
gives 4
uo=alui..-I-
_,
aiui--al
(5-54)
i--2
This
equation
The
points
greater
than
along
CD
along
HG
need
the
mesh
line below
HG.
In
below
holds
this
HG,
this
therefore,
equation
One mesh
point
interest knowns.
These
tions
144
values
so forth The
the
where
there
first
mesh to
stream
up to un at the
last
at a typical
point. point,
distance
in figure
s
5-12.
(fig. 5-8).
be applied
to each
is unknown
in the
region
equations
as there
are
points.
can be numbered
be ui at the
2 is on line
is a
FE
can
function
mesh
1
(5-55)
line below
of linear
are n unknown points
point
2,-s
just
gives
(5-55)
points.
The
since
are
for the first
aaus _ a4u4 -{- as
function
the
they
equation
as indicated
mesh
of u will then
equation
-_-
(5-52)
number
The
point
(5-46)
,_.
stream
as unknown
in n unknowns.
n. The apply.
that
or
same
points
to simply
Suppose
to the
(5-46) the
the
y-direction,
a_Na
since
AB.
be modified,
in equation
applies
for which
to give
referred
and
also
of equations
considered,
where
negative
condition
also.
along
must
Zto = alltl-_
This
be
point
us=u_._._-l,
2 in the
Substituting
not
corresponding
case,
point
(fig. 5-8)
At each
We then consecutively
first point, i, could
is unknown
will
have
point,
one
be
n equafrom
us at the second
be written
of un-
equation
I to
point, will
CHANNEL
1,2
H
FLOW
ANALYSIS
G
/
Ul "Ul, s - 1
FIGURE 5-12.--Mesh
point on first line below HG.
_"_aijuj
The
values
(5-55).
of the
All but
value
aij are determined five,
around
the
singular;
hence
there
of linear
These
of this
unknowns,
but
small,
roundoff
iteration,
few an
are type;
terms
initial
estimate
The
simplest
iterative
the
estimated
value
the
The
procedure
ever,
the
time the
equation
is simple
change When
The
w= 1, the
underrelaxation)
It
it always
iteration procedure is proven
is convergent occurs
when
After
this
at every
change
in the
for this
so that _, called
is straight
relaxation,
in reference
1 < _ < 2. In fact,
4 that
However, there
point
the
of
point, values
the of u. How-
computer
by increasing overrelaxation and
when
_:> 1,
overrelaxation the
is
so as to
problem.
greatly
start
consists
exci_ssive
by a factor
if 0 <:_ <2.
This
are To
mesh
is done
can be accelerated
of
requirements
in succession
converges slow,
systems number
methods.
unknown
point
non-
by iterative
in solving
is relaxation.
each
points
is always
are a large
iterative
every
The
= --1.
uj.
Storage
with
aii
be obtained
there
is negligible
is extremely
convergence
in u at each
it is overrelaxation. convergence
and rate
for the
equation.
procedure
there
the
through
unknown
valuable
is, where
of u at
and
aij matrix
can
of u at
point.
until
convergence
is required.
factor.
for that
is repeated
the
solution
is minimized
changing procedure
that
particularly that
(5-47)
outermost
(5-56)
in each
error
zero,
the
a unique
required. satisfy
for
to equation
techniques
equations and
is always
of equations
aij are
except
It can be shown
solution
techniques.
by one
of the
zero,
boundary.
A numerical
the
at most,
of ki is always
(5--56)
_-ki
greatest
is an optimum
(or rate
value
of of 145
TURBINE
DESIGN
between
AND
1 and
2 which
overrelaxation To give
APPLICATION
factor
gives
an explicit
use a superscript estimates
are
the
most
expression
on the denoted
ul. That
of ui°=0
calculate
ui re+l, for i = 1, 2,...,
--
overrelaxation
be any Then,
a solution
method), tions
for
Z
aijui
and
of ui. The example,
initial
an initial
for all i, we can
aij_J
m'gf-]gi-
(5-57)
uim
j-i-i-1
by
to calculate
(5-10)
For
we will
by
re+l-
u is obtained
it is necessary
(5-9)
value.
n in succession
optimum 4.
procedure,
if ui m is known
j-I
After
This
in reference
is, ui m is the m th iterate may
is satisfactory.
uim-_-0J
convergence.
as explained
for the
ui ° and
estimate
uim+l-_-_
rapid
can be calculated
the
overrelaxation velocities
(or
with
the
any
other
use of equa-
as
w(OZ) (5-58)
Yz-
pb and
o W_ =
The
partial
calculated
discrete
differences, the
values
or by
points.
The
at unknown from
fitting
mesh
As can
be seen,
of velocities puter.
which mixed
solution
analysis In
shown
in reference aqcordance
stream-function
method,
solution
The
146
region.
from the
the
been
flow must
TSONIC
program,
by finite
curve,
through
two
components is calculated
Analyses
The
and
the
which
is best
written
at the
through
5, can be used
the
the
either
velocity
equation
of these
the
from
angle.
procedure
in fig. 5-9). with
done,
Stream-Function
of flow
Most
estimated
as a spline
surface,
tangent
have
analysis
methods.
is described flow.
programs
(region
such
of Laplace's
calculation
for the
stream-function
blade
for
be
can be readily
blade
blade
Programs
computer
Center
the
must
is calculated
On the
and
the
au/Oy curve,
velocity
is a lengthy
Several
Research
a smooth
points.
one component
and
of ui. This
resultant
Computer
by
au/ax
derivatives
(5-59)
pb
are
program to analyze
be subsonic described
done
by com-
NASA
turbomachine
programs
constraints
calculation
for
called axial,
associated throughout in reference
Lewis blading
blade-toTURBLE, radial, with
or the
the entire 6, super-
CHANNEL
sedes
TURBLE
addition, flow
extends
the
problems.
gradient
called
analyze
8, obtains blade and
a detailed slot
MAGNFY
Flow indicated
by
fig.
MAGNFY
solution
in the
leading-
region
of tandem are or
in references
9 and
in reference
indicated
methods
of analysis
within give
possible sonic,
to use
called
indicated
the
intersect
method
depends
blades.
For
such
region,
defined.
On
the
in figure
guided
region,
must
other 5-9, and
of the suction
hand, less
surface.
alone
In this latter
can
than
is often equation
position.
suction
by
surface row,
surface
be computed
only
the stream-function
of the suction-surface
the
small
distribution blade
within
velocity
a
streamline
usefulness
and/or
suction
case,
other
of all
provided
to
is also sub-
give solutions the
velocity
and
to obtain
and
Therefore,
of the
It
analysis
ends
of the
subsonic
regime.
both
a low-solidity
half
by
subsonic
velocity-gradient
solidity
surface
velocities
definition
be obtained
assumptions
can only
where
(high
most
is
can be extended
flow
of flow guidance
for
than
which
equation
curvature
boundary.
4-11,
surface
be used if better
the
of analysis
associated
mixed-flow
entirely
velocity-gradient
because
passage
in figure the
solution
without
The
a passage
degree
as
potential-function
are
of analysis
solutions
a solid
on the
and
shown half
is,
a well-guided
as shown
guided
that
or stream-filament,
that
or
a preliminary
transonic
method
method
passage;
orthogonals
the
analysis
streamline,
A velocity-gradient guided
in
earlier.
a stream-filament
involves
surface,
can
and
the subsonic
solution
or supersonic
ones
flow
ANALYSIS
to solutions
a velocity-gradient
transonic, basic
TANDEM
By use of a velocity-gradient
however,
approximate
of any
The
_IERIDL,
solutions
stream-function
limited region.
assumptions,
an
the
are
the computation
additional
the
previously,
with
in reference
axial-
called
to extend
rows
flow.
of any
a program
VELOCITY-GRADIENT As
A
regions
blades.
hub-to-shroud
equation
a
solution.
7, can be used
described
to subsonic
10. Transonic
the use of a velocity-gradient stream-function solution.
to extend
or blade
and
5-1(a)),
by
a velocity-
section
rows
in
velocities)
using
or trailing-edge
(mean
fig.
be analyzed
by
or slotted
restricted
plane
supersonic
next
blade
called
4-14(b)
can
slotted
and,
stream-function
is described
or
meridional
turbomachine described
which
programs
in the
in the
subsonic
ANALYSIS
calculations
obtained
described
in tandem
or in the
same (local
are
flow rate)
program,
the
to transonic
type
mass
Another
all
solutions
TANDEM,
flow
splitters.
performs
solution
of the
(lower
program
it
Transonic
equation
preliminary to
in that
FLOW
of this turbine angles),
is within
the
can be well such
as that
is within on the
the front
analysis distribution
is required. 147
TURBINE
DESIGN
AND
APPLICATION
Method The
idea
sidering
of a velocity-gradient
a simple
case.
method
Suppose
narrow
passage
passage velocity
to be b, and the can be calculated
as shown
can
we have
in figure
be demonstrated
two-dimensional
5-13.
width d. If the approximately
We
by
con-
flow through
assume
the
height
mass flow is known, from continuity by
the
a
of the average
W
W.,o -
However, and
is a variation
in turbomachinery
With the
there
pressure
gradient
equilibrium,
where radius
in velocity
it is this
a force-equilibrium
it can be shown
across
velocity
equation, as was
(5-60)
pbd width
difference
by balancing
done
the
in chapter
of the
we are
passage,
interested
centrifugal
force
3 for consideration
in.
against of radial
that
q is the distance from of curvature for the
dW
W
dq
ro
the suction streamline.
(5-61)
(convex) surface, and The sign convention
re is the for rc is
important; rc is positive cave downward. For the
if it is concave upward, and negative if it is consimple case shown in figure 5-13, equation (5-61)
can be integrated
a radial
curvature
along
to be equal
for integration
from
line by assuming
in magnitude the
inner
radius W Wo
to the
passage
to any
point
the
streamline radius.
in the
148
results,
passage,
ro r
(5-62)
Row
FIGURE 5-13.--Flow
There
radius
through a curved passage.
of
CHANNEL
FLOW
ANALYSIS
where Wa
relative
r.
radius
of inner,
r
radius
of passage,
The
mass
velocity
on inner,
or suction,
or suction,
surface,
surface,
m/sec;
ft/sec
m; ft
m; ft
flow through
the
passage
w---
is expressed
rm+d
as
pWb dr
(5-63)
rl
and
substitution
constant
of equation
density
assumed,
(5-62)
into
(5-63)
and
integration,
with
yields w
w. =
In a similar puted
manner,
the
outer,
(5-64)
or pressure,
surface
velocity
can be com-
as W
-
Thus, by
using
not
an estimate
of the
equation
blade-surface
(5-62),
necessarily
(5-65)
which
restricted
to
velocities
is a velocity-gradient
two-dimensional
variation of velocity in the height of the be calculated in that direction also. We will now we are
consider
interested system
5-14.
indicated
Also
meridional
is a plane
angle
between
meridional
with
the
containing W_
plane.
and The
the the
x axis,
following Ws=
0, and
Also shown
and/_,
relations
the hold
W sin/_
W,_ = W cos/_
equation.
Since
angle
cylindrical
5-14
between
for the
in figure
W_, and
and W_. The in figure
are
some could
x, as shown W,,
of W,
We were
gradient
a rotating
axis
components,
resultant
x axis.
there
a velocity
we will use
velocity
W_ is the
If
velocity-gradient
r, angle
simply
equation.
flow.
passage,
general
radius
are
component
plane
a very
in turbomachinery,
coordinate
can be obtained
We. The
meridional are a, the W and
the
components: (5--66) (5-67)
Wr = W_, sin a
(5-68)
W_ = W_
(5-69)
cos a
149
TURBINE
DESIGN
AND
APPLICATION
W
FIGURE
In
5-14.--Cylindrical
addition
to the
r-, 0-, and
m-coordinate.
The
line,
in figure
as shown
line distance of the
The
radius
positive We
in
the
of curvature if the streamline
want
the
distance
along
constant
angular
velocity this
The
_0.
m-distance
The
of the of the
plane;
For
along
the
streamline that
is,
the
0-coordinate
streamline.
The
where sign
is r_ is
of rc is
upward. along
an arbitrary
case of constant
(rV_,)
d--q=a
stream-
is the projection
meridional
dW
an
stream-
true
is 1/rc,
the
to use
a meridional
is less than
streamline
gradient
curve.
components.
meridional
is concave
momentum
velocity
it is convenient
meridional
meridional
curvature
and
is the distance
5-15.
angle
system
x-coordinate,
m-coordinate
if the
a streamline
neglected.
coordinate
at the
curve. total
Let
temperature
q be the and
inlet,
dr
dx
dO
jq+b
dq +c--dq
(5-70)
where W
COS
ol COS 2
W sin _
arc
150
r
/_+sin
dW,n
a cos _ -----2_ dm
sin _
(5-71)
CHANNEL
FLOW
ANALYSIS
Meridional streamline7
_' rc
Q
m
r
J
_x Axis
5-15.--The
FIGURE
b = - W sin a cos 2 _+cos re
m-coordinate.
a cos/_
dW_______ dm
c=Wsinasin[3c°s[3+rc°s_(ddWWm These
equations
In using ential
any
A great
number
(5-73).
blades, tial
channel, For
as shown
(0) direction
distance We=0,
normal then
are
these
not
dO/dn=O
cases suppose
in figure to the
known
5-16, page). and
have
an
and
no velocity
We
can
l_=0.
from annular component
calculate q=n
Further,
dW/dn, in equation
from
figure
11.
a differ-
such
in advance.
can be obtained
Let
of reference to solve
parameters,
can be estimated
we
streamline.
(B14)
precisely
parameters
of special example, (into
and
it is necessary
streamline-geometry
8. These
(5-73)
+2_sina
(B13)
equation,
involving
a, and
for a guided
as equations
velocity-gradient
equation
vature,
to
are derived
).
(5-72)
as cur-
However,
reasonably equations
well. (5-70)
passage
with
no
in the tangenwhere
n is the
(5-70). 5-16,
Since
it can
be
Outerwall--, Meridional streamline-,
Llnner wall
FIGURE
5--16.--Annular
passage
with
no
blades.
151
TURBINE
DESIGN
seen
dr/dn
to
that
AND
APPLICATION
= cos a and dx/dn
= - sin a. Then,
from
equations
(5-70)
(5-73), dW_ dn
Thus,
for this
tion
case,
equation
W rc
(5-70)
reduces
Several
computer
machine
blading
NASA
Lewis
CTTD
program,
and easier
programs
by
This
CHANEL
flow
turbines
program
program
velocity
streamline
orthogonals
surface, rate.
form
of equa-
through
turbo-
as illustrated
(choking)
mass
medium-
definition
than blading,
sections
of the
The
to
mean-,
a specified surfaces
program
program
used
meridionaland
for an orthogonal
the
gives
indicated
only
mass
flow
along
the
maximum good
results
previously,
may
be needed
be obtained
more for low-
for fully
guided
15 for backward-swept compressors.
use
of
in this chapter,
for
the
not
for
known
the
which
a blade-to-blade
velocity-gradient a subsonic
turbine equation,
use
of the called
impeller vaned
as
stream-function
are
and
in
diffusers
plane
impeller
it
were analysis
turbine and
in
streamline
in advance,
on
lines,
impellers
for a radial-inflow
is to extend
is presented along
meridional-plane
or radial for
for a meridi-
program
straight
a radial-inflow
A program
meridional-
method
impellers
are
a computer fixed
to obtain
equation
lengths
programs 11
basic
centrifugal
along
Such
in reference
used
The
velocity-gradient
to base
equation
also been
solutions.
orthogonal
that uses quasi-orthogonals in reference 16.
viously
hub-,
to compute
As
can
have
the
the
quasi-orthogonals.
A further
channel.
mixed-flow
uses
convenient
centrifugal
along
13.
or mixedare
along
of these
be used
by this
plane
for
Since
velocity-gradient
reference
a number
blading.
methods
analysis
presented
for the
radial-,
tip
satisfies
general
passage.
14, which
more
to blade
which
more
equations to
is the to axial-
in reference
axial-,
hub
at the
years
by the
is described
in a flow solution
also
solutions
and blade-to-blade
orthogonals.
for can
high-solidity
Velocity-gradient
reference
5-17,
made
because
from
written
for many
superseded
to analyze
blade
been
12 and is limited
which
results
can be provided
solidity
onal-plane
from
program
flow rate to
used
Velocity-gradient
This
are
have
was
now been
be used
in figure
This
that
both
and
orthogonals.
passage.
plane
can
of flow
in reference
program,
variations
Computations
blade
has
analysis methods
One
compressors.
determine tip-streamline
the
is described
CHANEL
or
for
Center.
which
to use
The
152
simple
Programs
velocity-gradient
Research
flow turbines.
was
to the
(5--61). Computer
for
(5-74)
of
analysis
is described
mentioned solution
preto
obtain the
local flow
gradient
supersonic
angles
and
equation.
velocities. streamline Programs
for
FLOW
ANALYSIS
solution
is used
to obtain
subsonic
curvatures
method are presented in references in reference 6 for a blade-to-blade
Orthogonal
The
CHANNEL
required
transonic-flow
for
solutions
the
velocity-
based
9 and 10 for a meridional solution.
on
solution
this and
j,f
su Hace _/ /
su rface
.-Suction Tip
I surface
orthogonal
f Midchannel stream line--, i
Mean
Parallel to axis of rotation-_
i Hub
T
FIGURE
5-17.--Turbine
blades
with flow
three-dimensional
orthogonal
surface
across
passage.
153
TURBINE
DESIGN
AND
APPLICATION
REFERENCES 1. JOHNSEN,
IRVING
Axial-Flow 2.
A.;
AND BULLOCK,
Compressors.
COSTELLO,
GEORGE
Velocity
NASA
R.:
Method
Distributions
in
ROBERT SP-36,
of
O.,
EDS.:
Aerodynamic
Design
of
1965.
Designing
Compressible
Cascade
Blades
Potential
Flows.
with
Prescribed
NACA
Rep.
978.
1950. 3.
COSTELLO,
GEORGE
Detailed scribed
Velocity
1060, 4.
VARGA,
Procedure
Distributions
RICHARD
gram
S. : Matrix
THEODORE; for
for
in
L.;
AND
Design
JOHN
SINNETTE,
of
Compressible
Surface
Iterative
AND
Calculating
Cascade
Potential
Analysis.
MCNALLY,
Velocities
of a Turbomachine.
KATSANIS, on
ROBERT
CUMMINGS,
Blades Flows.
T.,
JR.:
with
Pre-
NACA
Rep.
1952.
5. KATSANIS,
6.
R.;
Computational
THEODORE:
and
NASA
a Blade-to-Blade
Surface
Inc.,
Revised
on
X-1764,
Program
Stream
I).:
Streamlines
TM
FORTRAN
Prentice-Hall,
WILLIAM
1962.
FORTRAN
Pro-
a Blade-to-Blade
Stream
1969.
for
Culculating
Transonic
of a Turbomachine.
NASA
Velocities TN
D-5427,
1969. 7.
KATSANIS,
THEODORE;
Calculating a Tandem
Blade
8. KATSANIS, face
NASA
and or
O.:
TN
D-5044,
WILLIAM
TN
Mixed-Flow
for
Surface
of
FORTRAN
Program
a Blade-to-Blade
Stream
l).:
Program
for Sur-
1969.
WILLIAM on
Program Stream
1969.
]).:
on
D-5091,
Streamlines
FORTRAN
a Blade-to-Blade
Region
the
FORTRAN
Hub-Shroud
Turbomachine.
for
Mid-Channel
I--User's
Flow
Manual.
NASA
1973.
THEODORE;
AND
MCNALLY,
Velocities
and
Streamlines
Calculating Surface
McNALLY,
NASA
Axial-
D-7343,
KATSANIS,
NASA
AND McNALLY,
Velocities of an
on
in a Magnified
THEODORE;
Surface TN
AND
of a Turbomachine.
KATSANIS,
WILLIAM
Streamlines
Turbomachine.
Velocities
Calculating
10.
and
THEODORE;
Calculating
9.
AND McNALLY,
Velocities
of an TN
Axial-
on
or Mixed-Flow
D-7344,
WILLIAM
1).:
the
FORTRAN
Hub-Shroud
Turbomachine.
Program
Mid-Channel
for Flow
H--Programmer's
Manual.
1974.
11.
KATSANIS, THEODORE: Distribution in the
12.
KATSANIS,
Use of Arbitrary Meridional Plane
Quasi-Orthogonals of a Turbomachine.
for Calculating NASA TN
Flow D-2546,
1964. THEODORE;
Method Blade. 13.
for NASA
KATSANIS,
NASA
TM
TN
of Analysis
VANCO,
Meridional D-6701, 16.
KATSANIS,
154
GINSBURG,
Design.
Choking
for Flow
AMBROSE;
Flow
NACA
R.:
Plane
of
for
an
Axial
Flow
Turbine
Quasi-Three-Dimensional for Turbomachine
CalBlade
Rows.
Rep.
AND
Through 1082,
FORTRAN a Turbomachine.
OSBORNE,
WALTER
Mixed-Flow
M.:
Centrifugal
Method
Impellers
1952.
Program
for
CMculating
I--Centrifugal
Velocities
Compressor.
in NASA
the TN
1972. THEODORE:
Distribution D-2809,
Quasi-Three-Dimensional
A
1971.
T.;
MICHAEL
T.:
Velocities
Program and
for Compressible
of Arbitrary 15.
Velocities
D-6177,
JOSEPH
LOIS
1967.
FORTRAN
of Surface
HAMRICK,
DELLNER,
Blade-Surface
X-1394,
THEODORE:
culation
14.
AND
Calculating
on 1965.
a
Use
of
Arbitrary
Blade-to-Blade
Quasi-Orthogonals Surface
in
a
for Turbomachine.
Calculating NASA
Flow TN
CHANNEL
FLOW
ANALYSIS
SYMBOLS A
flow area, mS; ft 2
ai
coefficients
b
cascade
height,
m; ft
d
passage
width,
m; ft
h
distance
between
ki
constant
in equation
m ?t
distance distance
along meridional streamline, normal to streamline, m ; ft
P
absolute
pressure,
q R
distance
along
r
radius,
8
blade
T
absolute
t u
time, sec stream function
V
absolute
W
relative
W
mass
flow rate,
fluid
absolute
for equation
(5-46)
mesh
points, (5-56)
N/m2;
J/(kg)
(K);
m; ft
2
curve,
m; ft
(ft)
(lbf)/(lbm)
(°R)
m; ft spacing,
m; ft
temperature,
velocity,
K; °R
m/see;
velocity,
m/see; kg/sec; angle
(in the tangential distance in direction 0
angular
distance
P
density,
kg/m3;
potential
ft/sec ft/sec lb/sec
of inclination
meridional plane, deg fluid flow angle, relative
o3
lb/ft
arbitrary
gas constant,
m; ft
to blades,
direction), deg of outer normal
in direction lb/ft
from
direction
in the
of the
meridional
plane
to cascade
boundary,
out
of rotation,
axial
m; ft
rad
a
function
angular velocity, tad/see verrelaxation factor
Subscripts: c
curvature
in
inlet
m
meridional
component
n out
component outlet
normal
p
pressure
r s
radial component suction surface
x
axial
y
component
in y-direction
z
component
in z-direction
to streamline
surface
component
155
TURBINE
8
DESIGN
AND
tangential
APPLICATION
component
o 1 mesh-point 1, 2, 3, 4 I
156
designations
CHAPTER 6
Introductionto BoundaryLayerTheory By WilliamD. McNally As shown
in chapter
certain
amount
ducing
work.
work
of ideal The
causes. on the
the
next
chapter.
the and
layer
hand,
This
that
more
of the
(windage),
chapter
provides
turbine
is not
a
for
pro-
converted
to
important
and
difficult
to understand
their
losses.
losses.
_Iethods
fluid
as air)
the
influence
there
velocity
agree
of the
on the
outer with flow
fluid
edge those
basic
are
viscous
presented
a turbine
blade
flow is confined of the
of this
blade.
layer
loss in the
At
is zero in all directions
layer
is called
flow is frictionless,
with the
at normal
to a relatively
This
the
calculated
assumptions.
to estimate
LAYER
past
neighborhood
At the
nonviscous)
flows
the
partial-
to boundary-
needed
losses
BOUNDARY
of viscosity
immediate
layer.
mixing
and
introduction
the parameters
and
a real in the
an
incidence,
for determining
trailing-edge
(such
flow
gives
to calculate
OF
conditions thc
friction
is used
boundary
(frictionless,
to the
energy
of the
a turbine
it is necessary
NATURE
velocities, thin
disk
associated
When
One
predicted,
which
(friction)
and
is available
ideal
is the prediction
be
operation.
theory,
viscous
can
flows,
admission
that
of the
across
primary cause of losses is the boundary layer that develops and end-wall surfaces. Other losses occur because of shocks,
tip-clearance layer
design
losses
The blade
ratio
to be a loss.
of turbine
Before
pressure
energy
portion
is considered
aspects
2, the
the
wall, (no-slip
use on
of ideal
the
other
condition). 157
TURBINE
DESIGN
AND
It is the frictional, velocity
from
point
layer
layer
at the
and
or viscous,
slide
over damped
ness of the
overall
or changes
in some
Most are
flows
to a turbine, The
on the
bulent
boundary
layer.
amplified,
as in turbulent fashion Figure layer.
6-1
a boundary The
a mean also
Separation layer
manner
stream a turbine
blade,
the
shows separates, this
static
Laminar boundary
the along
pressure _- Transition _ region
for any
great
dis-
becomes
disturbances
a turin the
in velocity
boundary
oscillates
layer,
in a random
moves
away
rear
portion
turbulent
boundary
boundary from
the
layer. blade
in figure
6-3.
of the
suction
increases.
This
Separated -,,_,,a, lull
FIGURE 6-1.--Boundary
_'
_Z////'_
layer
\
on blade.
When surface.
As the free-
r-Turbulent boundary layer
__
158
a the
layer --....
_,
have flow,
and
in the
laminar
correspondingly
/
a combustor,
fluctuations
is illustrated the
time
overall
turbulent
point
region in the
fluid
happens
with
6-2 (b) indicates.
a separated occur
are
smooth-
of velocity
weak
random
any
steady
laminar
In the
at
as figure
can likewise
decreases
flow.
blade
in velocity
this
region
region,
to the
velocity
value,
in which
velocity
leads
to the
it from
With
remain
transition
of turbulent
flow,
about
flow.
suction
indicates.
components
of
The
is always
on the
is either
a transition
In the this
influence
or entering
cannot
through
and
are characteristic
fluctuations
6-2(a)
the
layer
parallel
local
as figure
type
blades
passes
layers
6-1.
stagnation
both
negligible
fuctuating
in this
along
fluid
wall.
at the
boundary
at a point
ducted
It usually
that
velocity way,
tance. flow are
Any minute have
grows
the
in figure
thickness
fluid
reduce
to zero at the
of the
layer,
smooth
in nature. layer
and
portion
they
flow. The
influence
boundary
other.
that
is illustrated finite
blade
boundary so that
being
turbulent
significant
blade
initial
layer
value
a small
of the
The
each
sufficiently
frictionless from
edge
surfaces.
In a laminar
surface
in this thin
on a turbine
develops
leading
pressure
laminar.
forces
its free-stream,
A boundary boundary
APPLICATION
region-t
surface positive
of
INTRODUCTION
TO
BOUNDARY-LAYER
THEORY
Steady Steady t
t
I
Unsteady
t (a)
Laminar
t flow.
FxovaE
(b)
6-2.--V_riation
FIoUrtE
pressure
gradient
boundary
layer
layer
in a direction point. can
The also
turbulent
laminar
layers
boundary can
be
Mach
laminar
equati()ns
for
and the
layer This
be noted
either
the
immediately
layer.
it should
lew_'l ()f the sent
and
that
Just
turbulent incompressible
closc
flow passing
the
itself
at the
leading
edge
reattach both
itself in figure
laminar
and
or compressible, as there
are
boundary-layer and
different flow,
compressible
flow
in the
to the
reverses
incompressible
number.
the
flow
flow
is illustrated that
The
very
of the mean
which
boundary
separatc
Finally,
at
flow.
at a point.
retards
energy.
a degree
to that
point
gradient)
it to lose
to such
Turbulent
time
separation.
pressure
causes
opposite The
with
6-3.--Boundary-layer
(adverse and
can be retarded
separation.
of velocity
in
wall it moves blade.
is the
This
the
is
separation
of a turbine
to
the
boundary
blade
surface
as
a
6-4. turbulent
boundary
depending equations there
are
variations
on
the
to repredifferent of each. 159
TURBINE
DESIGN
AND
APPLICATION Turbulent boundary Separat ion
Laminar
bubble;,
boundary layer_
layer 7 _
,Z__...1-f_.rrt_
II I I __I __' ' .....
c Stagnation point
FIGURE
6-4.--Laminar
separation
Boundary layers should be considered relative Mach number exceeds values equations
for these
discussed
in this
various
The
general
OF
equations
equations.
equations, equations
In
compressible of 0.3 to 0.4.
are derived
of motion of the
be derived
from
be repeated
here.
of viscous
fluids
systems,
coordinate
directions.
the
tion
assumptions
are
represents
methods
the
for a compressible
during
Navier-Stokes fluid with
du dt
1 and
their
The
are
The
the
equations, The
combined
such
Navier-
the law of conis lengthy, and
have
derivation.
Navier-
three
boundary-layer
equations.
2 both
equations
constant
the
are
by applying This exercise
different forms. of the Navier-Stokes
made
are called there
Navier-Stokes
References
derivation, in two somewhat There are various forms what
solution
EQUATIONS
coordinate
Stokes equations themselves can be derived servation of momentum to a fluid element. will not
and
if the free-stream The boundary-layer
BOUNDARY-LAYER
normal
one for each can
reattachment.
chapter.
DERIVATION
Stokes
cases
and
complete
depending following into
vector
on equaform
viscosity:
gf_g__ Vp+_U V2u+ p p
__
p
V(V.u)
(6-1)
where u
general
t
time,
g f
conversion
160
general
velocity
vector,
m/sec;
ft/sec
sec constant, body
force
1;32.17 acting
(lbm)
on a unit
(ft)/(lbf) mass
(sec _)
of fluid,
N/kg;
lbf/lbm
INTRODUCTION
P
density,
P
static
/z
dynamic
In this
kg/mS; pressure,
s
N/m2;
lbf/ft
viscosity,
equation,
u, v, and
lbm/ft
three
BOUNDARY-LAYER
THEORY
2
(N) (see)/m
u represents
w in the
TO
2; Ibm/(ft)
a general
coordinate
(see)
velocity
directions
vector
with
x, y, and
components
z, respectively.
u=uiTvj+wk where The
i, j, and total,
k are
the
or substantial,
unit
vectors
derivative
(6-2) in the
three
of u is du/dt.
coordinate In any
directions.
of the
coordinate
directions, d
0
0
0
0
Oz In equation
(6-1),
rather
than
vector
quantities, du _ -_=g'--p
operator If the
(6-1)
V2 is applied
term
_
which
be more
[VX(VXu)-]+_
in terms
familiar
to the
p-f-_- grad(div P
vector
into
u
simple
1
VP+U-o V(V.u)--p V operator
to the
V2u is expanded
becomes
g
the
du gf-'q grad d--/= p
Laplacian
function.
equation
Expressing may
the
to a scalar
(6-3)
u) -_-
of gradients, reader,
p
curls,
and
equation
(6-4)
u)
1 _l P grad
curl(curl
(6-4)
p- V(V.u)
+_
divergences, becomes
(div
u)
(6-5) In
order
to derive
the
to be expanded
into three
directions.
three
Ou
Ou
The Ou
+U x+V y+W
boundary-layer scalar
resulting
equations,
equations, equations
Ov
Ov
Ou Op __u /O_u _z-z=g f . .... gpox p t0_-t-
Ov
g Op __u_/O2v
of the
(6-1)
has
coordinate
are 02u 02u\ _y2+0-_)
l u 0 [Ou
Ov
equation
one for each
020
Ov
Ow\
Ov
Ow\
02v\
-_-t- u -_x -k-v -_y + W oz = gf u ....
l u 0 [Ou
161
TURBINE
DESIGN
aw
aw
AND
_
APPLICATION
g Op.
+ w aw
tt [CO2w. O_w.
COho'_
1 tt cO[cOu
cOy
cow\
+5-_ t,_+_+_)(6-s) P
where
f,, fv, and f, are the
In
order
Laminar
Incompressible
to
Prandtl's
incompressible (1)
derive flow,
Viscosity
writing
of the
(2)
the following
assumptions has
the final terms
in equations
Flow
and
Layer equations
for
laminar
will be made:
already
been
assumed
in the
Since
for
incompressible
flow
the
con-
is
V. u=div
(3)
f.
equations.
/cOu
as well
cOy
cOw\
u=t_x+_yy+_z (6-6)
to (6-8)
is two-dimensional.
consideration,
force
Boundary
This
is incompressible.
equation
of the body
boundary-layer
is a constant. preceding
Flow
tinuity
components
This
as all terms
)=0
(6-9)
can be eliminated.
eliminates
involving
equation
(6-8)
from
w or O/cOz in equations
(6-6)
(6-7). (4)
Flow
is steady.
(5)
Body
forces
Thus,
f, andf_
With
these
following
This
are
eliminates
negligible
can be discarded assumptions,
two equations
cOOr terms.
in relation from
the for the
to inertia
equations
and viscous
(6-6)
Navier-Stokes
and
equations
(6-7). reduce
COy
the
continuity
(6-11)
. _ . t,_+_)
equation
becomes cOu
cOy
_x+_yy=0 In order
to make
boundary-layer and
flow,
the
some
velocities
and
check
are negligible coordinate
(6-10)
equations
an order-of-magnitude
show that
162
equations
the
(6-_0>
g__ cOp + __ / cO_v cO2v\
u_+__: Likewise,
to
x- and y-directions:
COu cOu /O_u CO'u\ u_+v _= 00p __ ___,,_,_+_)
COy
forces.
with
directions
(6-12/
to (6-12)
suitable
are traditionally is performed respect pertinent
for the analysis made
on
to others. to the
the
of
dimensionless,
various
Figure boundary
6-5
terms
to
shows
the
layer.
INTRODUCTION
U =u uO_
TO
u_5 _
BOUNDARY-LAYER
full
THEORY
Trailing
y
x
L
FmURE 6-5.--Boundary-layer
The
following
dimensionless
velocities
parameters
and dimensions.
are defined:
X X
(6-13a)
=-
L
(6-13b)
u
(6-13c)
U0
(6-13d) Uo
(6-13e)
Re = o.L
Uo (6-13f)
where X
dimensionless
x-coordinate
L
characteristic
length
Y
dimensionless
y-coordinate
U
dimensionless
velocity
u0
free-stream
V
dimensionless
velocity velocity
(in this case,
the blade
chord),
m; ft
in x-direction upstream
of blade,
m/see;
ft/sec
in y-direction 163
TURBINE
DESIGN
AND
P
dimensionless
Re
Reynolds From
And order
figure
since
APPLICATION
pressure
number 6-5,
we see that
y is proportional
$r,m/L
the y-direction x-direction. In order quantities,
to the
= _, a quantity
U0, U = u Uo is of order in the
to put (6-12)
equations
are
much
equations
are
(6-10) and
is multiplied
(6-11)
1 /O_U
02U\
OV
OV
OP
1 [02V
O2V\
are
of order
of magnitude with
each
by
resulting
OP
those
of the
L/Uo _, and
(6-15)
OV
various Since
in the
dimensionless
.....
other.
in
of dimensionless
multiplied
The
OU
_--_+_-_ order
are
L/Uo.
Y is of
velocities
than
in terms
1.
u is of order
_, since
smaller
to (6-12)
by
OU
be compared
much
_/,u,
since
OU
u +v
The
thickness
1. Likewise,
V = v Uo is of order layer
(6-10)
to L, X is of order
boundary-layer less than
1. And
boundary
equations
equation
since x is proportional
= 0 terms
X and
(6-16) in these
equations
U are of order
1, and
can
now
Y and
V
e, OU 1 -- =-= OX 1 OU ----OY
1
(6-17a)
1 (6-175)
oV OX
- = _ 1
(6-17c)
1
(6-17d)
OV --=-= OY
O_U 1 -=-= 1 OX 2 1.1
164
O_U
1
1
0 y2
e- e
e2
(6-17e)
(6-17f)
INTRODUCTION
TO
BOUNDARY-LAYER
THEORY
a2V
e ----- E 0X _ 1.1 02V
_
OY _ Furthermore, magnitude order 1. Relating to (6-16)
the
change
as the
change
these
--
of
orders
1 -
_.e
in P with
(6--17g)
(6-17h)
e
respect
U with
to X is of the
respect
of magnitude
same
to X,
so that
terms
in equations
to the
order
OP/OX
of is of
(6-14)
yields OU
OU
v
OP
1 /02U
v o-T=
(6-18)
i3-X+
(1) (1) + (e) (!)
= -- 1 + (_)
OV
OP
OV
v
02U\
(1+_)
1 /02V
+ v oT= or
+
(1) (_) + (E) (1) = -_+
OU
02V\
)
(6-19)
(t2) (_+!)
OV
(6-20) 1+1 By examining can be reached: (1)
In
terms
(6-18),
1Re
02U/OX
2 and
Reynolds (2)
is to dominate, smaller fore, allows
than P=P(X)
(6-20),
must
be must
02V/OX
the
_, the
it too must OP/OX,
and that
two
since terms
with terms
this
the
conclusions
viscous
terms
of magnitude
to be true 2 is much
as the
in equation larger
than
Therefore,
the
large.
are
and
that order
02U/OY
of
of order
order
and
e. Therefore, a function
OP/OX=dP/dX
pressure
_
e or less. Therefore,
P can be considered the
following
in parentheses.
l/Re
be of order
or p=p(x),
us to assume
d,
be relatively
(6-19),
same For
of order
dominates
the
it is assumed
2) -] are of the
U(OU/OX)+V(OU/OY).
equation
dominating
to
theory,
2) + (02U/OY
number In
(6-18)
boundary-layer
1/Re[(O2U/OX inertia
equations
across
with unless
2.
OP/OY
OP/O Y is much of X alone.
or Op/Ox=dp/dx. the
02V/OY
boundary
layer
ThereThis in the 165
TURBINE
DESIGN
y-direction
the
_, the
(4)
In
small
constant.
existing
Since
order
APPLICATION
is essentially
flow pressure (3)
AND
at the
first
equation
second
equation
equation
(6-18),
in comparison
It can be assumed
outside
of the
is of order
1, and
can be neglected 02U/OX
with
02U/OY
_ can
2. This
equal
boundary
to the potential
layer.
the
second
equation
is of
completely. be
neglected
leaves
the
because
following
it is so dimension-
less equations: OU OU dP 1 02U U _ T V O----Y = - d--X -{-Re 0 Y_ OU
(6-21)
OV
OX +-_=O These
are
The the
Prandtl's
boundary-layer
boundary-layer
influence
for different
From
number
equation
magnitude, the viscous-force smaller. The boundary-layer decreasing
layer
by
The
Uo/L.
useful
in determining
of the
boundary
we see that
layer
as Re increases
be
(6-21)
equations Ou u --+v Ox
increasing
viscosity
can
equation
resulting
are size
rule,
laminar,
Prandtl's
decreases.
put by
Ou
g dp
-
Oy
_t
p dx
in terms Uo2/L
of
and
dimensional
equation
(6-22)
_ 02u
(6-23)
p Oy 2
Ov
incompressible
flow.
and equations (6-23) It should be noted the
presence
of large
boundary
layer
shock Mach
viscosity
waves
(i.e.,
where
occur).
on mainly
the
about
the
interaction
two-dimensional,
arc assumed surface, unknowns
for their equations
instantaneous Just
as
flow
Reynolds
of shock
waves
constant
dp/dx, is also are u and v,
calculation. arc not valid adverse
in
pressure
phenomena
number,
wave depend on primarily the Mach number. number is not included in the boundary-layer
us nothing 166
and
for
along the blade The remaining
(6-24) are sufficient the boundary-layer
magnitude
depend
equations
Density
gradient solution.
and that
of shock
gradients
(6-24)
boundary-layer
and known. The pressure known from an ideal-flow
to
the thickness
--+--=0 Ox Oy are
and So,
are
Ou
These
in
Re corresponds
So, as a general
as the
equations
by multiplying
form
Furthermore,
decreases
variables
form.
on the
(6--21)
if pL Uo is constant.
boundary-layer
in dimensionless
terms (1Re) (02U/O y2) will get smaller thickness will correspondingly decrease.
_i_u decreases.
viscosity
of the boundary The
in this
Reynolds
fluids.
as Re increases,
equations
equations
of the
(6-22)
in the
conditions
in a
Since the influence of equations, they tell and
boundary
layers.
INTRODUCTION
The
boundary-layer
is approached. velocity
v is much
boundary
layer
Nonetheless, right
significant
than
and
up
to the
separation and
calculations
The
Navier-Stokes
However, in the
close
v begins
to the
error these
since
used
is quite
question flow
over
can
(i.e.,
the
y-axis
be derived
reference of curvature
terms
r at a position of the
as was
previously.
thickness for the the
such
x along
individual With
is small
compared
with
no large
variations
same
boundary-layer the walls
as would
as well, occur
near
radius result
sharp
there
for
surface.
of the curved equations are
given
in
radius
relative
orders
in the same
manner
the
boundary-layer
of curvature
of the
occur,
no large
for
system
on the
The
that
as were
The
change
coordinate
so that
obtained
equations are
negligible). would
equations
in curvature
boundary-layer
provided
be used development
dependent
assumption
equations
fiat-plate
are
These
arc very
the
of
for an orthogonal system of each of the coordinate
can be estimated
the
V is
point
set of Navier-Stokes
the blade
terms
not
is in the direction
a system.
equations
case where
Therefore, curved
in such
where
flow region.
orthogonal
the x-axis
as u. in cal-
of the
equations
to it, a new
in the
region
in the
effects
If a curvilinear
wherein
of magnitude done
curvature
boundary-layer
is normal
for flow
1. The
the
wall.
is introduced
and
where
as to how
a curved
(fig. 6-6) wall
large
arises
the
order used
should
of the boundary-layer equations were derived of coordinates in which the radius of curvature axes
the
the
point,
same
of a separated to (6-8)
is that
separation
location
equations
(6-6)
as separation
generally
in the
neighborhood
equations
are
THEORY
derivation
to be of the
point,
little
reliable
in their
equations
small,
is incurred.
detailed
BOUNDARY-LAYER
completely used
u. Very
rapidly,
boundary-layer
is very
separation
are net
assumptions
smaller
grows the
culations
equations
One of the
TO
may variations
wall,
and
dr/dx
._ l,
for fiat bc
walls.
applied
to
in curvature,
edges.
y x
x
Y
FIGURE
6-6.--Curvilinear
coordinate
system
on
a blade.
167
TURBINE
DESIGN
AND
APPLICATION
Laminar An
Compressible
order-of-magnitude
equations
and
neglected, case,
analysis
for a compressible
viscosity
density
and
can
assumed
energy
temperature,
the equation
of state
temperature,
and,
is required.
nonisothermal, can
be
thermal
In the
not
used.
For
boundary-layer These
are
compressible of
and density
to
for
three
viscosity,
were
a function
form
equations
flow will involve
to temperature.
the
pressure some
case,
variations
is considered
to relate
the
incompressible
temperature
viscosity is used
to derive
of the energy compressible,
parameters specific
which heat,
and
conductivity.
There The
The
was
Layer performed
is not isothermal,
variable-viscosity
related
layer.
equation constant,
if the process
be
constant,
is no longer
equation
also
boundary
were
the
density
Boundary
are
most
several
common
relations
for viscosity
is probably
Sutherland's
as a function relation
of temperature.
(rot.
1)
z [T_3/2To+S _=\-_o] T÷S
(6-25)
where _o
dynamic
viscosity
T
absolute
To
reference
S
a constant,
Ibm/(ft)
A less
power
reference
temperature,
temperature,
K; °R
K; °R (for air, but
also
S=
by
heat
and
least-squares
perature the
less accurate,
and
for
viscosity, 168
one
equations
for
be related
the
variables
relating
component
of the
to temperature
particular related
gas
problem
these
variables
momentun_
and
tem-
to temperature, reduce
will be the equation,
the
to u, constate
equation. analysis
equations equations
can
fits these
0.65.
compressible-boundary-layer
the energy
incompressible the
conductivity With
order-of-magnitude
(Navier-Stokes) that
in the
cquation,
The
thermal
T. The four
equation,
relation
(6-26)
For air, _0 is approximately
involved.
unknowns
tinuity
temperature-viscosity
0.5
polynomial-curve
range
v, p, and
110 K or 198 ° R)
law
_ is a constant.
Specific
To, (N) (sec)/m_;
K; °R
_o= \_o/ where
temperature
(sec) static
complicated,
is the
at the
for flow.
of the
continuity
compr,.ssible For
analogous
flow
con,pressible to _()-10)
and
momentum
is almost flow
to (6-12)
with
identical nonconstant
are the
following:
to
INTRODUCTION
Ou
Ou
Op,
TO
BOUNDARY-LAYER
THEORY
0 [
L2" ou ---- 2
pu _+ pv oy--= -g _-v_
Ov\l O [ IOu Ov\l
[Ou
(6-27) Ov
Ov
pu _xx+P,
g Op.
Oy
0 [
Ov
/Ou
2
Ov\l
a [.lay
au\l (6-28)
O(pu)
+O(pv) Oy
Ox If an order-of-magnitude to that layer
for
the
analysis
on these
equations,
the
equations
following
similar
boundary-
result:
pu -_x-{-pv --=--g Oy
o(pu)
-d-x-t--_y
equation
(6-30)
-0
Ox
boundary-layer
_
o(pv) +
The
(6-29)
is performed
incompressible-flow
equations
=0
(6-31)
Oy
of state
is also
required
flow. The
state
equation
for the
solution
of compressible
is
p=pRT where
R is the
The
final
gas
constant,
equation equation,
The
energy
equation
for
the
energy
equation
for
magnitude
check.
two-dimensional
pc,
in J/(kg)
required
momentum
and
The
the
(K)
besides
a perfect
=_xx-i-_Oyy.Oxx
Cp
specific
at constant
J
conversion
k
thermal
continuity
energy gas,
written
the
equation.
is derived
of another
equation
k_-x)T_yy
energy
layer
means
(°R). equation,
is the
boundary by
flow of a perfect
U_xxTV_yy
(ft) (lbf)/(lbm)
of state,
gas
is the
or the
equation
a compressible
following
steady
(6-32)
from
order-of-
for compressible, in full:
k_yy)+_j_
(6-33)
where heat
constant, conductivity,
pressure,
J/(kg)
(K);
Btu/(lbm)
(°R)
1 ; 778 (ft) (lbf)/Btu W/(m)
(K);
Btu/(sec)
(ft) (°R)
and
j
(6-34)
169
TURBINE
DESIGN
AND
APPLICATION
If an order-of-magnitude
check
following
energy
boundary-layer
is performed equation
on the
above
equations,
the
results:
(6-35)
Equations layer
(6-30),
equations
(6-31),
thc
ideal
It is desirable blades.
Turbulent
motions)
superimposed
present. the
are due
magnitude flow.
are
The
sional,
flow
first
those
since
stretching ever, handle
motion
the
to represent
per-
(mixing
or
eddy
fig. 6-2). are
important,
since
of velocity
are
of turbulent
of the
time-dependent,
is a prime
These
not feasible
at
the
in
stresses
often
of greater
boundary-layer three-dimen-
three-dimensional could
mechanism
available of these
fluctuating
their
motion.
The
solutions
the
will
in
(see
solutions
portion
separation
decrease
motion
calculations
computers
the major
turbulent,
solution
solution
which
three-dimensional
mesh
fluid
mean
equations.
over
fluctuations
is very
to the
exact
largest
is not
components
two-dimensional
of eddies,
even
flow of
Methods
layer
closed-form
due to the
Navier-Stokes
required,
main
that
approaches
is the
boundary-
compressible
a resulting
irregular
on the
mixing
two
with
has
to fluctuating
than
There
layer
blades,
so complex
Yet,, the
fluid
the laminar
Solution
boundary
boundary
the
formance. fluctuations
a turbulent
If the on
are
two-dimensional,
Boundary-Layer
to have
occur
(6-35)
gas law.
Turbulent
probably
and
for nonisothermal,
a gas obeying
of turbine
(6-32),
never
equations
arc
represent
the
of turbulent
at
the
present
equations
flow.
How-
time
cannot
on a small
enough
components
of velocity
the equations
of continuity,
of turbulent
flOW.
The and
second
energy
approach
density,
temperature,
of the
u component
velocity temperature
is to write
in terms
of mean and
and
velocity.
of velocity,
of fluctuation are written
by
fluctuating
u'.
In for
So the
170
fluctuations
approach,
example,
the
is denoted
velocities,
of pressure,
density,
time by
average
_ and
pressure,
the and
as follows: u = _+ u'
(6-36a)
v=_+v'
(6-36b)
p = _+
The
this
momentum,
components
in viscosity,
(6-36c)
p'
p = p + p'
(6-36d)
T= T+
(6-36e)
thermal
T' conductivity,
and
specific
heat
are
INTRODUCTION
negligible
and
as functions If the
are not considered.
of the
listed
momentum,
and
continuity, compressible These They the
flow,
are called are
unknowns are
the
turbulent where
u'v' is the
terms
in the
problem
available.
the
stresses,
For
substituted
this
for the
equations
relations and
following
over
time
of
additional
additional
equations
expressions
stress
terms
or
before
th_
can be solved. Boundary (6-36)
performing
equations
and stresses.
add
empirical
Reynolds
of equations
then
average
the
equations.
or Reynolds
for which
Incompressible
(6-12),
in thees
equations
reason,
into
incompressible
arises
new
Substituting
flow:
for
terms
pu'v',
Turbulent
layer
equations
of stress
v'. These
boundary-layer
yields
are substituted
pu '_ and
are
and
(6-36)
form
approximations
(6-11),
energy
boundary-layer
are calculated
of temperature.
in equations
set
THEORY
parameters
of u r and
presently
turbulent
three
"apparent"
to the
not
a new
value
BOUNDARY-LAYER
the
of the
product
So these
time-averaged
flow properties
TO
for
Layer into
equations
(6-10),
an order-of-magnitude
turbulent,
analysis
incompressible,
boundary-
(6-37)
(6-a8) These flow.
equations Notice,
momentum (_ and
are analogous however,
equation.
_), thereby
the This
(6-28), magnitude pressible,
the
(6-29),
presence adds
making
Turbulent Substituting
to equations of the
a new
three
unknowns
(6-32),
analysis boundary-layer
and the
(6-33)
and
following
term
in the
two
two
equations.
Layer
(6-36) then
for laminar
to the original
only
Boundary
(6-24) stress
(u'v')
with
of equations
yields
and
Reynolds
unknown
Compressible relations
(6-23)
into
equations
performing
equations
for
all turbulent,
(6-27), order-ofcom-
flow:
o(_)
ox
. o(_,)
, o(p'v')
+
-o
(6-39) (6-40)
/5 =_RT
(6-41) 171
TURBINE
DESIGN
AND
APPLICATION
1
where
T, is the
absolute
0
_
total
k
0_
0
temperature,
(6-42)
in K or °R, and
is defined
T,= + We
have
now
dimensional,
laminar
boundary-layer the
point
equations
for
SOLUTION velocity
parameters Included
and as
are
presently exist circumstances.
After
basic
far
profiles
defined,
the
basis
tions the
time
that
for the
many,
boundary-layer
are
discussed of
flat-plate,
the
for
two-
and
compressible
this
is really
solutions
are
many
only
concerned.
methods
solutions
BOUNDARY-LAYER
some
under
which various
EQUATIONS
and
the
solution
important
methods
incompressible
boundary-layer will
solution,
be
discussed.
as well
as com-
boundary-layer
solu-
methods.
of the
principal
is a description blade
surface
results of the
(fig. 6-7).
FIGURE
172
equations
incompressible at this
boundary-layer
Velocity One
boundary-layer
note
as
only
OF
(6--43)
turbulent,
obtaining
will be the
pressible
the
flow. We should
starting
These
derived
as
Profiles
obtained velocity
The
profile
velocity
6-7.--Boundary-layer
from
most in the
profile
velocity
boundary
describes
profiles.
layer
along
mathematically
INTRODUCTION
TO
BOUNDARY-LAYER
THEORY
Outeredgeof boundarylayer_ /
!
°e:J
|
u J
la)
/ (b)
IlL rll//llllTII/I/,
U/1/:frillill/I1
(a) Laminar profile, FIauaz 6-8.--Laminar
the dimensionless y/5:,,,
from
at a distance stream
velocity
the blade. y from
velocity
_],m,
from
from
the
velocity,
the
at
a
the
surface.
blade
where
surface,
u is the and
distance the
the
equal
Alternately,
profiles
of the velocity velocity
to _:_,
velocity
for laminar
shape,
while
those
monly
used
mathematical
for turbulent
by Pohlhausen
u-a The
as a function
velocity
the by
distance
in the boundary u, is the defined
1 percent
free-
thickness,
as that from
layer
external
boundary-layer
is often
differs
dimensionless
the
distance external
u,.
Velocity
originated
u/ue
The
(b) Turbulent profile. and turbulent velocity profiles.
constants
_-}-b
a, b, c, and
flow
(fig. 6-8(a))
flow are
expression
for
tend
to be parabolic
blunted
(fig.
u/ue
in laminar
6-8(b)). flow
in
A comis that
(sec ref. 1) :
( ,_y+c ( ."__ Y+ ( :,y d are defined
in terms
of a dimensionless
(6-44) shape
parameter
u
dx
(6-45)
wherc }, a = 2 +-6
(6-46a)
k b = -- 2
(6-46b)
X
c=
(6-46c) 173
TURBINE
DESIGN
AND
APPLICATION
Shapeparameter,
;:!-
o. 1
==
0
FIGURE 6-9.--Laminar
veh)city
d = 1 ---
Velocity
profiles
Velocity law
for various
profiles
values
for turbulent
Pipe-flow
experiments
Reynolds
number appropriate
n can
be related
to other _fand
Definitions Solutions
In
of the
order
thickness to
define
thickness
of the
thickness
is rather
boundary
layer
little
distance 174
a value from
exponent 4 up
5, the
however, which the
wall.
since because
is very
close
It is possible
0, and
the
from
place
the
the
the
are
most dis-
factor
H.
define
the
of boundary-layer velocity
in the
external
to define
dis-
are the
form
asymptotically.
velocity
to the
the
are described
to first
definition
transition
it takes
namely
These
it is necessary The
exponent
equations
parameters.
thickness
8/,,n.
The
Parameters
boundary-layer
layer,
of n= 7
0, which
Boundary-Layer
important
of the
value
plate.
parameters, thickness
momentum
outside
power
function
10. The
flow on a fiat
parameters,
arbitrary, to that
by the
n is a mild
to about
boundary-layer
of three
these
represented
(6-47)
the momentum
boundary
importance,
attains
the
from
two-dimensional
in terms
often
6-9.
_
of Important
obtained
placement
that
varies
shc, wn in figure
kS/,,H/
for boundary-layer
placement thickness in the next section.
often
show and
(6-46d)
flow are
Ue
profiles.
6
of _ are
-- =
is most
1.0
.2 .4 .6 .8 Fraction of boundary-layer height, y/Sfull
inside This
boundary
velocity boundary-layer
at
the is of layer
a small thick-
INTRODUCTION
TO
BOUNDARY-LAYER
THEORY
ue Ue
,-(u e - u) ue
r/Ill,
rllllilllllllll
(a) Actual
velocity
FzGva_
ness as that from
the
The
distance
profile.
external
from
the the
pe is the
outward
5, for
compressible
the help of figure 6-10. flow within the boundary
density, layer.
5, the
distance
velocity
differs
by I percent
boundary-layer
flow,
As seen from figure 6-10(a), layer due to the influence of
by
boundary
distance
the
for
u,.
thickness
_[ass
where
Equivalent profile equal mass flow. of a boundary layer.
thickness
where
'llll[lll//
'lllll/ll/llfll
(b)
the blade
velocity
displacement
is given
llill,
6-10.--])isplacement
can be defined with the decrease in mass friction
(b)
(a)
II!_1111/_
defect
in kg/m This
which
3 or lbm/ft
external
as a consequence
of the
on)
defect
decrease
free
stream
outside
can be represented
as shown potential
(6-48)
dy
3, in the
mass
thickness,
the
(p,u.-
t/=81u.ll
integrated
displacement by
=
in figure field
6-10(b).
of flow
in velocity
of by a It is
is displaced
in the
boundary
layer. As figure
6-10
shows,
the
distance
_ can
be defined
by the
equation
[.y=Sfutt
(p.U.--pU)
dy
(6-49)
y--O
Solving
for _ gives
= -- 1
[_-,s.,,
(p.u.--
peue _u-O
The
displacement
thickness
The
for incompressible
friction
is given
dy=
_ y--O
loss of momentum
dy
(6-50)
0
_=-- 1 f_,=_, `n (u.--u) Ue
pu) dy = IJ_:z"':"u (Pp-_u_) 1 -flow reduces
f.=',,<,,
(_)1--
to dy
(6-51)
_ _0
in the
boundary
layer
due
to the
presence
of
by 175
TURBINE
DESIGN
AND
APPLICATION
y= I/ull
l"
Momentum
defect
= I
pu( u,--
d
This
momentum
defect
can be represented
from
the
by a distance
momentum
0, defined
p,u,20 =
u) dy
(6-52)
y=0
of purely
by the
pu (u,--
Y=PJfull
potential
flow
equation
u) dg
(6-53)
" y=0
Solving
for 0 in this equation
ness for compressible
boundary
0=-LIe2
_
momentum
as the
1--
ratio
y=0
dy=
-y=0
(6--54)
to
1--
dy
(6-55)
l"/e
compressible
of displacement
dg
flow reduces
] "
both
thick-
pc_le
for incompressible
H for
momentum
as
y=0
factor
of the
dg=
u(u,--u) /_e2
defined
layers
_
thickness
form
definition
y=0
0=-The
the
pu(u_--u)
Pe
The
gives
and
thickness
incompressible
to momentum
flow
is
thickness:
5 H =There
are many
other
two-dimensional, These
boundary-layer
and
especially
three,
however,
are
boundary-layer
studies. Physical
When retarded toward
of flow
fluid in the
boundary
exists
along
penetrate small
a surface,
too
kinetic
far
and
moves
behind
the point
the
principal
from
a region
stream.
follow
neighborhood
of the
wall.
the
occurs,
176
6-11
illustrates
separation
general
particles
layer
cannot,
pressure
pressure
the
the
gradient
of the surface
gradient in general,
because
is deflected
In general,
stream. The and reverse
some
pressure
away fluid and
of their from
the
particles move
in a
point of separation is flow in the layer in the
At separation,
_yy/_=0=0 Figure
H for layers.
in
from
an adverse
fluid
main
used
away
of increased
opposite to the external as the limit between forward
immediate
or a casing with
retarded
of separation
boundary
parameters
is transported
the boundary
the
_, 0, and
of Separation
a blade
layer
region
Thus, into
besides
for three-dimensional,
the
When the
into
energy.
surface direction defined
stream.
parameters
Interpretation
separation the main
(6-56)
0
occurring
(6-57) along
a surface.
INTRODUCTION
TO
(;),.o >o
,_\\\',, .....
FIOURE
By relation the
Prandtl's
between
it is possible presence
dp/dx>O.
being
- -- _x_
as flow
boundary-layer
pressure
gradient
to infer
that
of an
adverse
From
surface
gradients
separation
equation
undergoes
and
flow
gradient with
the
and
velocity
in a steady
pressure (6-23),
separation.
equations
dp/dx
TItEOR_/
-o
LSeperation point
6-11.--Velocity
examining
BOUNDARY-LAYER
(i.e., boundary
considering
distribution
u(y),
will occur
only
decelerated
can
dp/dx
conditions
at
relate
through
velocity
equation
velocity
\Oy_/__o
= g dx
profiles
to
(6-58).
neighborhood
02u/Oy 2, depends of the
the
u = v = 0, we have
now
immediate
in
flow),
dp We
the
of the
only
on the
profile
at
The wall,
the
pressure
the
(6-58)
Ou/Oy,
O_u/Oy _, and
cquation
indicates
curvature
of the
gradient,
wall
changes
dp/dx, its
sign
that velocity
and
the
with
the
finally
to
in
the
profile, curvature pressure
gradient. Figure layer
6-12(a)
subjected
shows
a velocity
to a decreasing
profile
pressure.
that
would
For such
exist
a profile,
in a boundary figure
6-12 (b)
y
(c)
(a) Velocity profile, FIGURE 6-12.--Velocity
(b) Velocity gradient, distribution
in a boundary
(c) Velocityprofile curvature. layer with pressure
decrease. 177
TURBINE
DESIGN
indicates
that
Ou/Oy
Furthermore, Ou/Oy,
AND
figure
is negative
profiles
is positive 6-12(c)
are
not
all
y and
that
dp/dx.
pressure
(6-58),
as y increases. slope
that
negative
a boundary
dp/dx)
of impending
is the
we know
Consequently,
(negative
indicative
decreases
02u/Oy _, which
equation
to negative
to a decreasing which
for
indicates
for all y. From
02u/Oy _ corresponds subjected
APPLICATION
will
layer
have
separation
of
velocity
(the
form
of
fig. 6-12(a)). Figure with
6-13(a)
gradient). near
shows
decelerated the
flow
Here, blade
corresponds be less than
a profile due
figure
6-13 (b)
surface;
which
to an
that
would
increasing
indicates
for which
layer
velocity
02u/Oy_= profile.
O. This
It follows
in a boundary (adverse
Ou/Oy
is, O_u/Oy _ is positive
to positive dp/dx. However, zero at some distance from
point
that
exist pressure
is a point that
has
a positive
slope
(fig.
6-13(c)).
This
since in all the surface,
cases there
of inflection
in a region
layer pressure
O_u/Oy 2 must must exist a
of the
of retarded
boundary-
potential
flow
• j Y
:::_/-Point of inflection
(a|
(b)
TRY-
FIOURE
_y2 .
(a) Velocity profile, 6-13.--Velocity
distribution
(b) Velocity gradient, in a boundary
(c) Velocityprofile curvature. layer with pressure
Stagnation
Sudion -_'_"_Adve
Fmuug
178
6--14.--Pressure
distribution
rse gradient
on a turbine
blade.
increase.
INTRODUCTION
(positive
dp/dx),
the
point
of inflection.
(with
8u/Oy
that,
with
can
adverse Figure
6-14
when
the
used
the
indicates The
It was
a typical danger
This
(ref.
On a fiat plate
3).
point
will have of separation
of inflection,
equation
a
it follows
(6-23), (i.e.,
distribution
on the
separation in regions
of
first
was
steady
separation
Layer
of a is
the major
in 1928
fiat-plate
as an
Therefore, therefore, 8u
8u
82u
u _+v
o_
oy=
viscosity
,/p,
0U
in m'/sec
of
(ref.
Prandtl's in 1908.
4).
the velocity
is constant
reduce
Technical
of Blasius
by NACA p(x)
Plate
NACA
solution
solution
translated
a Flat
in 1904 in Germany.
flow at zero incidence,
equations,
where
on
mathematical
the
is constant.
surface
is concerned,
surface,
first reported
published
The
kinematic
as
place.
was
was also later
The boundary-layer
v is the
THEORY
layer
is retarded
Boundary
and
with
solution
where
a point
of the suction
theory
to be published work
as far
is taking
translated
German
potential
pressure
portion
diffusion
Memorandum equations
at the
flow
zone,
boundary-layer
later
profile
in deriving
Incompressible
Prandtl's
boundary
have
potential
seen to be the rear of the blade
Laminar
in the
velocity must
BOUNDARY-LAYER
gradient).
blade.
readily
profile
surface)
assumptions
only
pressure
turbine part
Since
= 0 at the the
occur
velocity
TO
and
from dp/dx
the ffiO.
to
(6-59) or ft'/see,
and
¢9V
(6-e0) The
With
following
the
differential
are
use
the boundary u=v=O
at
y=O
U=Ue
at
y=
of a stream
equation
conditions:
function
(6-59)
into
(6--61) oo
_b, Blasius the
following
transformed ordinary
the
partial
differential
equation: f d2f+2 dy 2 where
f is a normalized
stream
daf=0 dy 3
(6-62)
function
f(,)179
TURBINE
which
DESIGN
depends
AND
APPLICATION
on the dimensionless
y-coordinate, Y
=
This
equation
has
the
following
n, where
(6--64)
boundary
f=_--fy=O
conditions:
at
n=O
(6-65) df _=1 dy Equation mate
(6-62)
solution
cannot
in the
asymptotic
expansion
able
More
point.
(6-62)
with
df/dy, the
and
degree
profile at the
wall
series
expansion
two
solutions
(ref.
of accuracy,
turns
oo
Blasius
Howarth
of figure and
the
_=
exactly.
of a power
for ,1 = _,
recently,
a high
be solved
d2f/dy _ as functions
velocity
curvature
form
at
6-15.
This
profile
rather
abruptly
.4
.6
about
71= 0 and
at a suit-
the
Blasius
equation
tabular
= u/u_,
the
possesses further
values
gives
a very
small
from
it in order
E .2
.8
1.0
Boundary-layervelocity ratio, u/ue Fmuaz 180
6-15.--Blasius-Howarth
velocity
for f,
solution
!_ s-. 0
an
joined
provided df/dy
an approxi-
being
5) solved
and
of 7. Since
obtained
profile for flow on a flat plate.
INTRODUCTION
to reach
the
inflection,
asymptotic
since
From
the
value.
At the
BOUNDARY-LAYER
wall itself,
the
curve
has
THEORY
a point
of
for y = O, O_u/Oy _= O.
order-of-magnitude
boundary-layer
TO
equations,
analysis we had
the
performed
to obtain
Prandtl's
relation
(6-66) For a semi-infinite
flat plate,
the
Reynolds Rez-
number
can be expressed
u,x
as (6-67)
p
In order
to make
equation
(6-66)
dimensionally
x2
correct,
we can say
(6-68)
Rez
or
_is.u ¢c
The
constant
solution
of proportionality
and is equal
in laminar
flow,
(6-69)
can be obtained
to 5. So, for a semi-infinite
we
obtain
the
useful
from Howarth's flat plate
relation
for
numerical
at zero incidence
the
boundary-layer
thickness
(_s_zz=5.0 With
the
ing relations
use of Howarth's for other
flow on a flat plate
solution
important
v/_
to the Blasius
boundary-layer
(6-70) equations, parameters
the
follow-
for laminar
can also be obtained:
= 1.72
0=0.664
gr,, pUe 2
= 0.332
v_
(6-71)
v]_
(6-72)
0.332
_/"-:-_U_g
(6-73) =
1.328 D = _ b _¢/-_plu2 g
(6-74)
181
TURBIN]_
DESIGN
AND
APPLICATION
1.328
(6-75)
CI = 1.328 _-_ "uJ where I"W
shear
D
total
b
width
of fiat plate,
l
length
of fiat plate,
Cf
dimensionless
Re_
Reynolds
It should flow;
stress
on the surface,
drag
on both
equations plate
then
will
are valid
Rez < 106, a value
will probably
larger
occur,
for laminar
that
and the
is indicative expressions
the leading
to turbulent than
only
For Re_ > 106, transition
only from
If transition be
for fiat plate
l
of the plate.
will be valid
point.
drag
length
relations
length
layer
to (6-75)
the
N; lbf
coefficient
on plate
only where
the entire
to the transition
occur,
based
all of these
boundary (6-71)
_
m; ft
are valid
flow over
to turbulent
of fiat plate,
drag or skin friction
that
that is, they
lbf/ft
m; ft
number
be noted
of laminar
sides
N/m_;
boundary
that
calculated
Solving
the
in
edge of the layer by
does
equation
(6-74). Integral
M_thods
for
Laminar-Boundary-Layer The tions
two are
principal by
integral
means provide cumbersome. Integral
means
methods
of solving
methods
approximate are
and
based
Von
K_rm_n's
original
was
later
translated
by NACA
was
not
necessary Instead, in the
boundary layer,
only
are
over are
the
integrated thickness
introduced,
pressible
over the
the
differential
y=O
(6-50))
following
of fluid
equation
equation
(eq.
thickness. to y=_/,,n, and
momentum
equations
realized
result.
close
in the
(6-23)
the
a mean
(6-30)) (6-23)
definitions
thickness For
to the
boundary
Such or
it
fluid
by satisfying
is satisfied.
if the
that
for every
If equations and
integral
in 1912 in Germany
Khrm_n equations
region
Both
extremely
momentum
flow is approached
remaining
are
equations
boundary-layer
(eq.
laminar,
by and of dis-
(6-54)) incom-
flow,
dO+ (20+,_) u2 dx
182
6). Von
equa-
methods.
solutions
Khrm_n's
boundary-layer
boundary-layer from
exact
was published
(ref.
the
momentum
(eq. the
yon
external
In the
a mean from
integration placement
where
finite-difference
since
work
the
he satisfied
conditions.
is obtained (6-30)
to satisfy region
by
on
and
wall and
the laminar-boundary-layer
solutions,
formula.
particle.
Equations
u. du. = gr._.._. d'---x p
(6-76)
INTRODUCTION
For laminar,
TO
THEORY
compressible flow, uJ d_ + (20+_-MJ0)
where
BOUNDARY-LAYER
the subscript
e denotes
u, du, d--_ = pT._2_ p,
conditions
at the outer
(6-77)
edge of the boundary
layer. Equation for the
(6-76)
boundary-layer
sumed
for the
placement
at the wall, a solution
published
in
Pohlhausen
families
1921
7 and earlier
Pohlhausen's
distributions pressible
form
profile. and
exact
and
the
profile
shearing to
work
was
assumed
by
"Velocity
the simplest,
As a result, by
dis-
(6-76)
His
under
method
with
the
use
that
does the
Pro-
it is known
various
authors
assuming
solutions
not require
different was
solutions
velocity
for
laminar
incom-
solution
of ordinary at the wall,
a type
quantities
for the
relation
gradients.
of
known
its derivative
of these
that
all
specifying
universal
pressure
the
wall shear, forms
of exact
Pohlhausen's
compared
without
a nearly
favorable
and
approximate
method
nondimensional
It developed for
velocity
followed
collected
to one another
To do this,
quantities
layers.
chapter,
his
which
He relates
factor
evaluated
layer.
those
Thwaites'
equations.
the
The
pressure.
extend
Thwaites
from
differential and
among
8).
flow.
0, and
is asthe
distributions.
work (ref.
thickness,
is probably
of rising
and
form
first to use equation
in this
solution
in regions
a suitable
us to calculate
boundary
1).
equation
allows
was the
(refs.
differential
that
This
momentum
discussed
of velocity
Thwaites
provided
incompressible
to improve
A famous
to an ordinary
u/u,.
T_. Pohlhausen
to give poor results tried
6, the for
was
Although
have
profile,
thickness,
obtain
leads
thickness,
velocity
stress
files."
or (6-77)
were
laminar
existed
For
of velocity defined
boundary among
adverse
these
gradients,
Thwaites selected a single representative relation. A unique correlation was chosen that reduced the solution of an incompressible problem to the evaluation
of a single
pressible heat
fluids
transfer
formation compressible One Their
best
and
by
the
method
applies or
pressure
Prandtl
symmetric
distribution
and
extended
recognized is equal
could
be
and
to date Reshotko
when
to 1, a transused
for the (refs.
or incompressible surfaces.
performs
to comthat to
relate
solutions.
to appear
of Cohen
to compressible
axially
10)
boundary-layer
is that
was
number
(ref.
methods
layers
method
(ref. 9). They
Stewartson
integral
boundary
stream
Thwaites'
Crabtree
to incompressible
of the
dimensional
and
is negligible, proposed
laminar
integral.
by Rott
It
flow
handles
well in areas
solution 11 and over
of 12). two-
arbitrary
free-
of adverse
pres-
sure gradient. A surface temperature level may be specified, and heat transfer is calculated. Cohen and Reshotko's method is based on Thwaites' correlation
concept.
Stewartson's
transformation
(ref.
10)
is first
applied
183
TURBINE
to
DESIGN
Prandtl's
equations the
equations.
wall shear,
the
Then
parameters by
The
surface
relations,
methods
In
to have
values
and and
for
Laminar-Boundary-Layer Finite-difference digital
come
computers.
work
with
and
this relatively
Clutter
short and
Turbulent referencing
boundary-layer length" used
flow,
should in many
stresses matical
form
which,
and the
pressure.
first
worked
of viscosity
14 and 16).
of
on the
computer.
for
recent give
very
in
solving
viscosity" to relate mean
into
the
only
transformed
of the
governing values
been
Reynolds of velocity a matheequations, of density,
equations
mean
in 1877.
law for laminar
the
values
differential
"mixing
have
are given
mean
turbulent
and
concepts
stresses
problem
of
Flow
to the
calculation
Another
methods
to date
containing
on this
in Stokes'
15).
of
amount
Concepts
"eddy
substitution
equations
development
These
approximation
Reynolds
for the
1.
the
the
methods
motion
the
a
which
from
a considerable
times
current
mixing
These
point
running
developed
means,
but
of
Mixing-Length
equations
starting
Boussinesq coefficient
the
published
boundary-layer
done
(ref.
These
upon
to differential
velocity, stitute flow.
this
have
concepts
methods
by
By
the
discussed.
of the
produced
components. leads
be
the
(refs.
of the
Young different
Boundary-Layer
any
important
Reshotko's,
Solving
because
of Krause
Eddy-Viscosity
Before
solving
technique
is that
carried resulting
Equations
prominence
Smith
of interest
results
for
into
in developing
reference good
methods
recently
the
of all the
slightly
Methods
of these
is then
11. With
Luxton
as Cohen
to
free-stream
quantities
calculation
1960,
is as general
Finite-Difference
have
transformed
of these the
related
interdependence
of reference
for
differential
parameters
and the
evaluation
number
first-order
of a unique
derived
13) which
Prandtl
transfer,
solutions
parameters.
(ref. the
The exact
are
boundary-layer method
heat
nonlinear,
of dimensionless
concept
is assumed. the
resulting
in terms
Thwaites'
utilizing
allows
APPLICATION
are expressed
velocity. out
AND
con-
boundary-layer
In analogy
with
the
flow
t_ Ou (6-78)
r,g Oy where mixing
rz is the coefficient,
laminar A,,
shear
stress,
in N/m s or lbf/ft
for the Reynolds
stress
in turbulent
2, he introduced flow by putting
A, 0_ r_ -
184
g 0y
(6-79)
a
INTRODUCTION
where
rt is the
introduced
turbulent
shear
concept
of eddy,
the
stress,
TO
BOUNDARY-LAYER
in N/m _ or lbf/ft
or virtual,
THEORY
_. In 1880, Reynolds
viscosity,
_, where
AY
, =--
(6--80)
p
Thus,
the
eddy
Turbulent
viscosity
stress
is analogous
to the
be expressed
as
can then
paa g Oy With
the use of this concept,
can be written
A similar
concept
eddy-viscosity
In
mean
1925,
free theory
itself
concept
good
deal
with
deals
the
with
Deriving
(6-82) than
and (6-40)
such
equation
where
as
an eddy,
difficulty
with
_ depend
on velocity.
between
applying
these
l is the mixing (6-81)),
the It is,
coefficients
1. His
Prandtl's
_ of the length
is generally is equation
more (6-81).
--P-
}-_y dy
mean kinetic
whereas
of large
clusters
of
stress
requires
a
shear
of turbulent
expression
to the is that
of particles,
motion
model
p l 2 Ida da --=
flow,
all of which
is (6-82)
U'V'
g
in m or ft. expression
that
little
first expression l of the
analogous
for
for
mixing-length
difference
motion
expression final
approximation
Prandtl's
main
macroscopic
of his physical
it appears
The
microscopic
the
length,
different
is called is somewhat
Prandtl's
in reference
On comparing
mixing
The hence
of gases.
g
viscosity
energy
relations
length
theory
rt =-
(eq.
and
argument
mixing
of discussion
is contained
where
(6-37)
a completely
His
the
concerns particles.
A,
empirical
introduced
kinetic
Prandtl's
is that
stresses,
in the
fluid
to the
can be defined.
to find
Prandtl since
path
(6--81)
velocity.
Reynolds
hypothesis,
p= u/p.
-Pu'v' g
in equations
be applied
method necessary
the
the
can
conductivity
therefore,
viscosity
as
or a virtual,
and
terms
kinematic
second
(eq. has
(6-82)) been
with that
gained.
has merely
been
expression.
However,
suitable Turbulent
for the dra_:
The
replaced
calculation is roughly
of Boussinesq unknown
by the Prandtl's
of turbulent proportional
eddy
unknown equation motion to the 185
TURBINE
DESIGN
AND
square
of velocity,
mixing
length
So, mixing
length
superiority
the
same
fluid.
local
It is far
1 than
about
of Prandtl's
integral
with
the
methods
since
was
the
first
for an incompressible in 1931.
improvements
to the
many
in 1949 and
empirical
was
relation
equation.
This
and
relation
transformations
10)
Maskell, pressible
in 1951
and
thus
obtained Tillmann pressure
to
the
equations
was
published
of them
empirical was
in 1950
in many
layers.
the
current
used
published
(ref.
in the
making
data
by
in Ger-
17), proposed
momentum
methods.
an
integral
Stewartson's
used
in many
methods
for solving
an
improved
method
for incom-
He replaced
approximation momentum
gradient.
determine
Truckenbrodt, translated
whose
by NACA
turbulent
and,
like
tion.
the momentum
which
thickness.
It
applies
Because
brodt's
equation
is directly A profile
method
is still
use
20).
Prior
been
utilized law,
of integral
to their with and
and
use
the
integrable parameter
is
the
of several
layers by
K_irm_tn
turbulent
Reshotko
and
momentum
boundary-layer empirical
first
equa-
symmetrical results,
Trucken-
boundary treated
integral
skin-friction
is simple
integral
layers.
adequately
Tucker
velocity
was
laminar
method
rotationally
were
adverse
for both
The
accurate
for incompressible
with
in 1952 and
momentum
and
relatively
boundary
an assumed one
not
flows
solutions flows.
two-dimensional
methods
work,
19), proposed
does
for
in Germany
boundary-layer
used
turbulent
point
published
(ref.
method, to both
was
of its simplicity
Compressible the
work
in I955
Maskell's
with
a separation
incompressible
flows.
186
turbulent solutions,
from an empirical auxiliary differential equation. The Ludwiegskin-friction formula is used to calculate the skin-friction disand
power
work
term
work
most
whose
proposed
determined
determines
tribution
and
18),
boundary
by an empirically
both
equations.
(ref.
turbulent
followed, and
likewise
the turbulent-boundary-layer
His
technique by NACA
are
the
for solving
layer.
skin-friction
is still used
(ref.
the
are
approximate
a method
Tillmann,
the
there
for solving
provide
of works
translated
for
the
the
equations,
boundary
calculational
Ludwieg
about
constitutes
Equations
methods
to propose
A rash
it is a
flow are now impossible.
turbulent
in Germany Gruschwitz.
Solving
of these
for turbulent
say
of Boussinesq.
Boundary-Layer
Both
this
if the
of velocity.
assumptions
_, and
that for
finite-difference
solutions
Gruschwitz
over
(6-82)
we cannot
to make viscosity
Methods
equations.
exact
although
laminar-boundary-layer
and
boundary-layer
eddy
from
of the magnitude
function,
expression
Turbulent as
is obtained
simpler
the
Integral
Just
result
to be independent
is a purely
of the
mixing
and
is assumed
length
property
APPLICATION
in 1957
(ref.
equation
profile,
had
usually
relations.
the
When
INTRODUCTION
pressure
gradient
of-momentum tiplying The
equation,
the
normal
was present,
integrand
to the
and
Tucker's
and
pressure
transfer
form
and
(ref.
10)
usually
used.
equation
is obtained
are and
momentum
transfer
(ref.
21).
by
by
auxiliary
mul-
a distance
to that
distance.)
equation
were
then
to compressible
flow
with
with
of Maskell
results is used
through
years
boundary
the
One
of
the
best
integral
an extension
the
same
and
moment-of-momentum
analysis,
simultaneously tributions
of the
Reshotko-Tucker
boundary-layer
boundary-layer
11 and 12)
source
analysis
is the
work
Finite-Difference
Finit_difference equations
portion Atwell
(refs.
28
Patankar
recently
begun
of this work have
29)
and
Spalding
is going
to date
based
on have
boundary-layer on in this
of Herring
(refs.
the
use
developed equations
field
at the
the
It
momentum are solved
shear-stress is better
dis-
turbulent than
of adverse program (ref.
compressible
Solving
is
somewhat
equations
and Mellor
for
that of pressure based on
22)
tech-
turbulent (ref.
24).
the
Equations
solving
the
turbulent
Cebeci
25, 26, and
methods
22).
uses
Sasman-Cresci on
today.
compressible (ref.
It
in regions a computer
to appear.
also developed
and
turbulent
for
turbulent
for
Cresci
analysis
and
until
of equilibrium
Boundary-Layer
methods
have
results
Methods
Turbulent
today
These
of information
where
programs
boundary-layer
numerical
point
method,
compressible
computer
to uncouple
Sasman-Cresci
(refs.
additional
as the This
method.
at predicting separation (ref. 23) has developed
Cohen-Reshotko An
The
the
and
is made of
recent
to simplify
for
equations.
introduction
analysis.
Reshotko-Tucker gradient. McNaUy niques.
no attempt
from
are used zero.
of Sasman
integral
after
the
available
is that
but
obtained
methods
through
is located
in many
concept
distribution
profile
available
layers
flow with
reference-enthalpy
becomes
used
Ludwieg-Tillmann
for compressible
Separation
best
moment-
transformation
The
shear-stress velocity
It is still widely
boundary
simply
the
18).
suitable
extrapolated,
and
in incompressible
of Stewartson's
of Eckert's
power-law
was
expressed
(ref.
in a form
equation.
ago,
are
use
for the
when
layers.
turbulent
the
application
and
friction,
several
also uses the momentum These
uncoupled
layer
skin
work
respect
applicable
the
moment-of-momentum
the
the
the moment-
equation
with
and
gradient,
An approximation
boundary
and
integral
integrating
equations.
relation
heat
large
(This
method,
integral
skin-friction
the
equation,
equation
and
of-momentum
the
THEORY
an auxiliary
then
integral
BOUNDARY-LAYER
simultaneously.
Reshotko heat
of the
surface
momentum
solved
was
TO
boundary-layer
and
Smith
27).
Bradshaw,
for the turbulent of the still (refs.
present
turbulent another
time,
energy 31).
and
done
a
Ferriss,
boundary
method
30 and
have
layer
equation. for handling
A great
no method
deal
of
is yet 187
TURBINE
clearly
DESIGN
AND
superior
(refs.
32
integral
and
to 33)
and
finite
APPLICATION
any
of the
compare
others.
many
difference,
for
Two
of
the
The
selection
of a method
problem
able. that of
This
can
have
been
solution
solution of
requires
the
the
be achieved mentioned
has techniques,
whole
been
herein.
the
variety
boundary-layer
methods,
turbulent
with
studying
intended
publications
prominent
suitable
familiarity
by
recent
boundary
both layer.
REMARKS
of solution
some
most
solving
CONCLUDING
layer
relatively
some
The to
various
of the
more
present
show
the
of methods problem,
to a particular the
recent
discussion
avail-
references
of the
historical
available, especially
boundarymethods
methods
development and
where
the
of
complexity
turbulent
flows
are involved.
REFERENCES 1. 2. 3. 4. 5. 6. 7.
HERMAN_ (J. KESTIN, TRANS.)" Boundary Layer Theory. McGrawHill Book Co., Inc., any edition. BIRD, R. BYRON; STEWART, WARREN E.; AND LIGHTFOOT, EDWIN N.: Transport Phenomena. John Wiley & Sons, Inc., 1960. PRAN_rL, L. : Motion of Fluids with Very Little Viscosity. NACA TM 452, 1928. BLASIUS, H.: The Boundary Layers in Fluids with Little Friction. NACA TM 1256, 1950. HOWARTH, L." On the Solution of the Laminar Boundary Layer Equations. Proc. Roy. Soc. (London), Set. A, vol. 164, no. 919, Feb. 18, 1938, pp. 547-579. YON K_RM_N, TH: On Laminar and Turbulent Friction. NACA TM 1092, 1946. POHLHAUSEN, K. : Approximate Integration of the Differential Equation of the Limit Surface of Laminar Motion. Zeit. f. Math. Mech., vol. 1, Aug. 1921, pp. 252-268. SCHLICHTING,
8. THWAITES, B.: Approximate
Calculation
of the Laminar
Boundary
Layer.
Aero-
naut. Quart., vol. 1, Nov. 1949, pp. 245-280. 9. ROTT, NICHOLAS; AND CRABTREE, L. F.: Simplified Laminar Boundary-Layer Calculations for Bodies of Revolution and for Yawed Wings. J. Aeron. Sci., vol. 19, no. 8, Aug. J,952, pp. 553-565. 10. STEWARTSON, K. : Correlated Incompressible and Compressible Boundary Layers. Proc. Roy. Soc. (London), Ser. A, vol. 200, no. 1060, Dec. 22, 1949, pp. 84-100. 11. CO_EN, CLAaENCS B.; AND RESHOTXO, ELI: Similar So|utions for the Compressible Laminar Boundary Layer with Heat Transfer and Pressure Gradient. NACA TR 1293, 1956. 12. COHEN, CLARENCE B. ; ANY RESHOTKO, ELI: The Compressible Laminar Boundary Layer with Heat Transfer and Arbitrary Pressure Gradient. NACA TR 1294, 1956. 13.
188
LVXTOS, R. E.; AND YOUNG, A. D. : Generalized Methods for the Calculation of the Laminar Compressible Boundary-Layer Characteristics with Heat Transfer and Non-Uniform Pressure Distribution. R&M-3233, Aeronautical Research Council, Gt. Britain, 1962.
INTRODUCTION
TO
BOUNDARY-LAYER
THEORY
14. SMITH, A. M. 0.; AND CLUTTER, DARWIN W." Solution of the Incompressible Laminar Boundary-Layer Equations. AIAA J., vol. 1, no. 9, Sept. 1963, pp. 2062-2071. 15. 16.
SMITH, A. M. O.; ANY CLUTTER, DARWIN W.: Machine Calculation of Compressible Laminar Boundary Layers. AIA_ J., vol. 3, no. 4, Apr. 1965, pp. 639-647. KRAUSE, EGON: Numerical Solution of the Boundary-Layer Equations. AIAA J., vol. 5, no. 7, July 1967, pp. 1231-1237.
17.
LUDWIEG, HUBERT; Stress in Turbulent
AND TILLMANN, W.: Investigations Boundary Layers. NACA TM 1285,
18.
MASKI':LL, E. C. : Approximate Calculation Two-Dimensional Incompressible Flow. Establishment, Nov. 1951.
19.
TRUCKENBROIYr,
E.:
A Method
and Turbulent Boundary Flow. NACA TM 1379, 20.
21.
for Calculation
of the
in Case of Plane and Rotationally
Layer in Aircraft Laminar
Symmetrical
ELI; AND TUCKER, MAURICE: Approximate Calculation of the Compressible Turbulent Boundary Layer with Heat Transfer and Arbitrary Pressure Gradient. NACA TN 4154, 1957. ECKERT, E. R. G. : Engineering Relations for Friction and Heat Transfer to SurRESHOTKO,
faces 587. 22.
Wall-Shearing
of the Turbulent Boundary Rep. AERO 2443, Royal
of Quadrature
Layer 1955.
of the 1950.
in High
Velocity
Flow.
J. Aeron.
SASMAN, PHILIP K.; AND CRESCI, Layer with Pressure Gradient 1966, pp. 19-25.
Sci., vol. 22, no. 8, Aug.
ROBERT
and
Compressible Transfer. AIAA
J.:
Heat
1955,
pp. 585-
Turbulent Boundary J., vol. 4, no. 1, Jan.
23.
MCNALLY, WILLIAM D.: FORTRAN Laminar and Turbulent Boundary NASA TN D-5681, 1970.
24. 25.
A Method of Calculating Compressible CR-1144, 1968. CEBECI, T.; SMITH, A. M. 0.; AND MOSINSKIS, G.: Solution of the Incompressible Turbulent Boundary-Layer Equations with Heat Transfer. J. Heat Transfer, vol. 92, no. 1, Feb. 1970, pp. 133-143.
26.
SMITH,
HERRING,
H.
Turbulent
A.
Layer 1967.
M.
JAMES;
AND
Boundary
0.;
AND
Equations.
MELLOR,
Layers.
G.
Program for Calculating Compressible Layers in Arbitrary Pressure Gradients. L.:
NASA
T. : Numerical Solution of the Turbulent-BoundaryDAC-33735, Douglas Aircraft Co. (AD-656430), May
CEBECI,
Rep.
27.
CERECl, T.; ANn SMITH, A. M. O.: A Finite-Difference Method for Calculating Compressible Laminar and Turbulent Boundary Layers. J. Basic Eng., vol. 92, no. 3, Sept. 1970, pp. 523-535.
28.
P.; FERRISS, D. H.; AND ATWELL, N. P.: Calculation of BoundaryLayer Development Using the Turbulent Energy Equation. J. Fluid Mech., vol. 28, pt. 3, May 26, 1967, pp. 593-616. BRADSHAW, P.: Calculation of Boundary-Layer Development Using the Turbu-
29.
BRADSHAW,
lent Energy Equation. Lab., Jan. 30, 1969.
IX: Summary.
Rep.
NPL-Aero-1287,
National
Physical
30.
PATANKAR, S. V.; ANY SPALDING, D. B. : A Finite-Difference Procedure for Solving the Equations of the Two-Dimensional Boundary Layer. Int. J. Heat Mass Transfer, vol. 10, no. 10, Oct. 1967, pp. 1389-1411.
31.
PATANKAR,
Layers. 32.
S. V.; AND C.R.C. Press,
SPALDING,
D. B." Heat
and
Mass
Transfer
in Boundary
1967.
COLES, D. E.; ANn HIRST, E. A., ED8.: Proceedings, Boundary Layers--1968, AFOSR-IFP-Stanford Press, 1969.
Computation of Turbulent Conference. Stanford Univ.
189
TURBINE
33.
DESIGN
BERTRAM, SP-216,
190
AND
MITCHEL 1969.
APPLICATION
H.,
ED.:
Compressible
Turbulent
Boundary
Layers.
NASA
INTRODUCTION
TO
BOUNDARY-LAYER
THEORY
SYMBOLS
A_r
turbulent
a
constant
b
flow mixing in eq.
coefficient,
(N)
(sec)/m_;
lbm/(ft)
(6-44)
m; fwidth of flat plate, ft constant in eq. (6-44)
Cf
skin-friction
e,
constant
cp
specific
D
total
d
constant
f
Blasius
dimensionless
f
general
body
coefficient in eq.
heat drag
for a flat
plate
(6-44)
at constant
pressure,
on flat plate, in eq.
J/(kg)(K);
Btu/(lbm)(°R)
N; lbf
(6-44) stream
force
vector,
function N/kg;
defined
by eq. (6--63)
lbf/lbm
component
of body
force
f in x-direction,
N/kg;
lbf/lbm
f, f.
component
of body
force
f in y-direction,
N/kg;
lbf/lbm
component
of body
force
f in z-direction,
N/kg;
g H
conversion
constant,
1; 32.17
(Ibm)
i
form factor, unit vector
defined by eq. (6-56) in the x-direction
J
conversion
constant,
J
unit
in the y-direction
k
vector
1 ; 778
(ft)/(lbf)
k L
characteristic
1
Prandtl mixing length, m; ft length of flat plate, m; ft Mach number external to the boundary
length
on the
(e.g.,
(K);
Btu/(sec)
the blade
turbulent
chord),
m; ft
layer
exponent
P
dimensionless
p R
static
Re
Reynolds
number
based
Rez
Reynolds
number
based
on l, as defined
in eq.
Re_
Reynolds
number
based
on x, as defined
by eq.
r
radius
pressure,
gas constant,
defined
N/m2; J/(kg)
velocity
(ft) (°R)
n
pressure,
lbf/ft (K)
of curvature
constant
in eq.
T
absolute
static
T,
absolute
total
To
reference
t
time,
U
dimensionless
Uo
free-stream
velocity
U
component
of general
(6-25),
eq.
(6-47)
(6-13e)
(lbf) / (lbm)
on L and
(°R)
U0, as defined
surface,
by eq.
(6-13f)
(6-75) (6-67)
m; ft
K; °R
temperature, temperature,
temperature
profile,
by eq.
2
; (ft)
of blade
S
lbf/lbm (sec _)
(ft) (lbf)/Btu
thermal conductivity, W/(m) unit vector in the z-direction
M.
(sec)
K; °R K; °R
used
in eq.
(6-25),
K; °R
sec velocity
in x-direction, upstream velocity
of blade, vector
defined m/sec; u in the
by
eq.
(6--13c)
ft/sec x-direction,
m/sec;
ft/sec 191
TURBINE
DESIGN
AND
APPLICATION
U
general
velocity
vector,
U.
free-stream
V
m/sec; ft/sec dimensionless velocity
p
component
m/sec;
velocity
at the
ft/sec outer
edge
in y-direction,
of the
defined
boundary
by eq.
layer,
(6-13d)
of general
velocity
vector
u in the
y-direction,
m/sec;
of general
velocity
vector
u in the
z-direction,
m/sec;
ft/sec tO
component
X
ft/sec dimensionless
Y
x-coordinate, m; ft coordinate parallel to boundary surface, m; ft dimensionless y-coordinate, defined by eq. (6-13b)
Y Z
x-coordinate,
y-coordinate, m; ft coordinate perpendicular z-coordinate, m; ft displacement
_yuu
eddy
surface,
m; ft
m; ft
thickness,
viscosity
by eq. (6-13a)
to boundary
thickness,
boundary-layer
defined
defined
m; ft
by eq.
(6-80),
m2/sec;
ft2/sec
¢
a dimensionless quantity much less than 1 Blasius transformed y-coordinate defined by 0
momentum
thickness,
dimensionless
viscosity,
dynamic
viscosity
Ibm/(ft)
parameter (N)
P P_
T!
lbm/ft laminar
Tt
turbulent
Tw
shear
viscosity,
a shear
time
at the wall,
defined by eq. stream function, in eq.
(6-26)
192
average
fluctuating
N/m2;
stress,
Superscripts"
t
m2/sec;
stress,
shear
stress
constant
2; lbm/(ft)
at reference
density, kg/m _; lbm/ft 3 free-stream density external
60
by eq.
(6-45)
(sec)
temperature
To,
(N)(sec)/m_;
(sec)
kinematic
function Blasius
defined
(sec)/m
p
_0
(6-64)
m; ft
shape
dynamic
eq.
component
ft2/sec to
the
lbf/ft
N/mS;
2
lbf/ft
N/m_; (6-34) m2/sec;
lbf/ft
_ 2
ft_/sec
boundary
layer,
kg/mS;
CHAPTER 7
Boundary-Layer Losses By Herman W.Prust,Jr. The
primary
builds are
up
the
friction
surfaces, blade the
cause
on the the
theory,
fluid. by
Chapter
means
analytically for
associated
the
A fundamental loss resulting
objective from
expressions
the
loss coefficients. as a fractional the
blade
subtracting
these
the
blade-row
efficiency
pressure 7-1.
proceeding
loss
coefficients, and
These
velocity pressure
the
coefficients
the
ideal based from used
discussion
blade-row
distributions and
The
theory
velocity
the
the
buildup and
presented
herein
refers
layers. losses
row.
the
Methods from
and
in chapter
of the
energy this
twoenergy the
of kinetickinetic
actual
flow
can be obtained is consistent
with
2. locations
will be introduced distributions
the
for
Therefore,
of boundary-layer station
the
loss in fluid
energy
on kinetic
be
losses
are in terms
express
can
experimental mixing
blade
kinetic unity,
high-velocity
is to minimize
chapter
the from
and
end-wall design
resulting
the
to boundary-layer
boundary
in this
definition
past
blades
analytical
of fluid through
coefficients
flow of fluid
trailing-edge,
in blade-row
of the
over
boundary-layer
blade plus discussed.
Efficiency
with
the
that losses
fluid
fluid with
covers
layer.
layer these
viscous
of the
blade-section
These part
row.
by
Before
surface
for loss developed
energy through
flow
from
friction,
boundary
energy
and
the
three-dimensional results are also
of the
an introduction
chapter
to two-dimensional
obtaining dimensional
final
the
This
determining
with
primarily
flow
boundary-layer 6 presented
boundary
In particular,
loss downstream
of which
described.
methods
the
of the low-velocity
free-stream
the
loss resulting
and
is the
surfaces.
from
pressure-drag edge,
in a turbine
and end-wall
loss resulting
trailing mixing
of losses
blade
with and
parameters and
the
associated
the aid of figure associated
dis193
TURBINE
cussion layer,
DESIGN
refer
AND
APPLICATION
to an attached
with its associated
higher Figure
loss,
and
7-1 (a)
cannot indicates
boundary
reversal
only.
of flow at the
be analyzed the
layer in the
four
station
A separated
surface,
same
is thicker,
manner,
locations
boundary
that
yields
if at all. will be referred
Station
,_---- $ --.--_
0
r la r"
'-1
(a)
.... --
Station 0
Total pressure Static pressure Velocity
I'--'--'I
_-r]
rq
v,,,,, .1| !,/ Station la
Station i
Station 2
(b)
FIovr_
194
7-1.--Station
(a) Station locations. (b) Pressure and velocity distributions. locations and associated press_Ire and
velocity
distributions.
a
BOUNDARY-LAYER
to in this
chapter.
Station
station,
a uniform
total
7-1 (b).
Station
boundary pressure stream
la
developed
profiles
as shown
value through
from
the
surfaces.
region value
pressure
Station
This
and flow angle la and
are
l, the
sufficiently associated profiles In
the
order been
inlet
conditions
both
free
stances,
constant
tests
but
and
seldom
the
exists
stream
and
boundary
a real
in the
the region
velocity _:,u. the these
to
downstream
mixing
downstream
state
fluid flows and
adjacent
over
the
boundaryfree stream profiles
static
pressure
Between
stations
at a distance
and
with
the
total-pressure
applications. do vary
at stations variation
of the
flow
in the last chapter
specifically used for obtaining be introduced and defined.
of
Experiments
somewhat and
across
1. In some
in-
can be accounted does
take
place,
a hypothetical
a loss results
and friction
for.
a com-
convenience.
surface. V:,
As shown varies at
the
layer,
certain
momentum desired
the
by
from full
zero
friction
layers
figure
7-2,
of fluid the
velocity
and
energy
thickness, here;
kinetic-energy
form
the
height
resulting
are used.
fluid
on
boundary-layer
parameters
and will be reviewed the
due to both
between
in flow, momentum,
thickness,
la
this
region
boundary
Uniformity
can be approached
PARAMETERS
velocity
the losses
of the
of variables
stations. usually
in actual
a surface,
to the
a number
various
is merely
surface
boundary-layer
free-stream
(displacement
introduced
as is
occurred.
mixing,
velocity
no
blade
la,
station-1
2 is located
that
layer
identified,
To describe presence
the the
too,
complete
and flow angle
will be later
fluid
in the
surface
the
station.
that The
BOUNDARY-LAYER When
with
discussion,
across
pressure
uniform
between
where
the
convenience
static
some
pletely
pl_ at the loss has
Here
freevaries
station
edge,
Station row
place.
analysis
that
which
Although
taken
is a universal
in component shown
has
blade
pressure
mixing by
the
is, of course,
across
region.
across
from
uniform.
assumed
have
constant
and
pressure
1 (b)
wake
loss occurs.
to simplify
have
little
The
Total
friction
trailing
in figure entire
of the
loss,
There
edge.
constant
where
blade.
in velocity
varies
surfaces.
At this in figure
of the
result
Velocity
trailing
blade
but
the
trailing-edge
mixing
edge
la, only the surface
assumed
are again
blade
row.
as indicated
surfaces
7-1 (b).
solid
is indicated
downstream
to the blade
trailing
is assumed
the void,
flow throughout
inlet
P']8.1,,= po' to the static
beyond
has filled
occurred.
showing
blade
a_o. At station
1 is just
fluid
the
on the at the
This
static
within
of the
free-stream
the
po' is assumed,
in figure
V:,.I,_ to zero the
the flow angle
has
is just
layers
flow
layer
0 represents pressure
LOSSES
from Some
factor)
in addition, coefficients
of
were others will
195
TURBINE
DESIGN
AND
APPLICATION
Free-streem velocit L Vfs
=i
,- Full boundary
W)odty, v
=;/
layer height.
¢////////.4,
_full
_'//////////_ Surface
FmuRz
The
7-2.--Typical
displacement
flow, is defined
boundary-layer
thickness
5, which
velocity
profile.
is indicative
of the
loss in mass
by
(pV) f. dY-
(0V)s,=L
_lul!
(pV)
dY
(7-1)
_0
where $
displacement
thickness,
boundary-layer V
fluid velocity,
P
fluid
Y
distance
()f.
free-stream
ary
is equal
layer
lb/fP normal
(ideal)
states
the loss in mass ideal
to the
The
momentum
the
196
layer,
m; ft
thickness
dy_
flow of the
which
would
pass
thickness.
fluid in the through
Solving
for
bounda length
_ yields
dY fo_:=u ...... pV (pV):.
O, which
(7-2)
is indicative
of the
momentum
by
O(pV_):.=Jo where
flow
displacement
['/"u =-o
loss, is defined
to boundary
conditions
that
to the
equal
m; ft
ft/sec
kg/m3;
in direction
(7-1)
(or an area)
m/sec;
density,
Equation
m; ft
thickness,
0 is the momentum
loss in momentum
fs:.u
(pVV/,)
thickness, of the
fluid
dy_
fo_,,u
pV 2 dY
in m or ft. Equation in the
boundary
layer
(7-3)
(7-3)
states
is equal
that to the
BOUNDARY-LAYER
ideal
momentum
an area)
of the
equal
to the 8=
The energy
loss
fa'"' -o
in kinetic
thickness
ideal
where
ff is the
energy
loss in kinetic
ideal
kinetic
(or an area)
equal
dY-
can
through
dY
(pV )i.
similarly
a length
(or
for 0 yields
PV_
fo s_'"
be
pass
Solving
(7-4)
expressed
in terms
of an
by
(pVV_,)
_0
thickness,
energy
energy
would
thickness.
pV (pV)t.
energy
defined
_ _b(pV_)/,=_
the
flow which
momentum
LOSSES
fluid in the
ideal
to the
energy
[6/.,, =-o
,V
flow
which
dy_
Ratios of the aforementioned
Equation
boundary
thickness.
(pV 3) dY
_0
in m or ft.
of the
of the
dY-
would Solving
fo sf"'z
(7-5) layer
pass
(7-5) states
is equal
through
that to the
a length
for ff yields
,V 3 dY (pV3)s.
(7--fi)
thickness terms are also used as basic
boundary-layer parameters. The form factorH isdefined as H=
Substituting dimensionless
equations
(7-2)
distance
y as
and
-_
(7-4)
y-
(7-7)
into equation
(7-7)
and defining
Y
a
(7-8)
_futt yields 1
1
(pV)I, H =
(7-9) 1
(or)f, An energy
factor
E is defined
(or'),,,
as E= _8
Substituting
equations
(7-6),
(7-4),
(7-10)
and
(7-8)
into
equation
(7-10)
yields
197
TURBINE
DESIGN
AND
APPLICATION
ff
pV (pV)/,
fo 1 -- pV 3 dy (pV3)I.
dy-
E=
(7-11) fo
Velocity profile
profiles
of the
(pV)j, pV
dy-- f[
for turbulent
flow
pV2 dy (pV_)1.
are
often
represented
by
a power
type V _yn
where
the
Note
that
profile
this
as
1In
the
numerical
exponent
power 6 (eq.
is here
(6-47)) as n,
that
to be used
often
between
expressed
is expressed
with
expressed equations
value
n is most
profile
is consistent
exponent
wherein the
of the
in chapter
pressed The
value
(7-12)
general
as yn, while as yl/n. The
derived.
for n will depend
with
exusage.
the
form
same
reference
Therefore,
on the
the
theory
is consistent
are
0.25.
exponent
boundary-layer
however,
follow
0.1 and
1,
specific
being
used
for
exponent. With
in series expressed ratio
this velocity form,
and
in terms
V/Vcr.
The
profile, the
form
of the resulting 1 --4 n+l
equations and
(7-9)
energy
exponent
and
factors
n and the
equations 3A f,
{
3n+l
) can be integrated
free-stream
derived 5A_.
(7-11
for turbulent
flow can be
critical
in reference
velocity
1 are
F'--
5n+1
H=
(7-13) 1
A/,
+
(n+l)(2n+l)
A_,
+
(3n+l)(4n+l)
-_--Jl*
(5n+1)(6n+l)
and
2
(n_l_l)(3n_q_l)--I-
(3n+l)(5n+l)+(5n+l)(7n+l)
E.__
1 (n+l)(2n+l)
t-
Af,
A_,
+
(3n+l)(4n+l)
-_+-
•
I
o
(5n+l)(6n+l) (7-14)
where
As._"/-
198
_+1
1 (_-)
2 _
(7-15)
BOUNDARY-LAYER
and
_, is the
constant
ratio
of specific
wlume,
critical
and
(Mach
approaches
heat
at constant
Vc, is the
1) flow
fluid
condition.
zero, equations
(7-13)
pressure
velocity,
to specific
in m/sec
For
incompressible
and
(7-14)
LOSSES
flow,
reduce
heat
or ft/sec,
at
at the
where
V/V,r
to
H_.c=2n+l
(7-16)
and 2(2n+1) E_._ =
Values
of the
form
and
energy
(7-17)
3n+l
factors
for turbulent
are shown in figure 7-3 for V/V_r varying from 0 to 1.5. It can be seen that the form
from factor
does
exponent
the
energy
is almost
layer
aerodynamic directly the
simpler ideal
from more
the
so
parameters"
n, the
type
presented
of body.
instance,
momentum to the
the
physical
could are
defined
pass on
They
n varying more than
energy
the
the
factor
work,
blade
row.
The
of zero
in
be ob-
however, row, it is
as a fractional
"dimensionless
can
useful can
of the blade
losses the
and
are directly
In turbine
termed basis
general
of a body
boundaries
through
herein
are
drag
thickness.
to express
that are
just
For
expressed
and
0 to 1.4 and varies much
flow
V¢r.
meaningful
quantities
parameters
constant
on any
work.
flow is confined
and
any
parameters
to a boundary
where the
of V
boundary-layer
certain tained
For
independent
The refer
factor.
compressible
part
of
thickness thickness
trailing-edge
thickness.
Free-stream criticalvelocity
ratio, (VNcr)fs f-0 //-0.6 2.2
-V/21.o ,,,,
hJ
_ 1.4-7
Power n usedin velocity equation VNfs =yn
,-0
L=
1.8 E"
-\\\
\ rL00 1
1.4
I 2
FIGURE 7-3.--Effect
r].25 ' _LS0
I 3
of compressibility (Data
4 Form factor. H
5
on variation of energy from ref. 1.)
6
factor
7
with form
factor.
199
TURBINE
DESIGN
AND
APPLICATION
"%..\ Station
_
_'_'_
t 8
____-_
_ J
Ys
_cos
ala
FIGURE 7-4.--Nomenclature
These
dimensionless
suction-
and
With the
the
in flow, corresponding
row
channel.
are
composed
the
thicknesses
parameters and
ideal total
of the
subscripts
pressure-surface
defined
flow conditions
thickness
The
must
region.
represent
the
sum
of the
are the
same,
thicknesses.
that
momentum,
the
where
parameters
pressure-surface assumption
dimensionless
losses
and
thickness
for trailing-edge
value,
boundary-layer
could
loss plus
by
the
channel
through
as indicated the
dividing
blade-row
pass
channel,
one
blade-
in figure
pressure-surface
by 7-4,
loss,
Stot=$,A-_p
(7-18)
Otot-- O,-.FOp
(7-19)
q/tot= _,A-_
(7-20)
p denote
total
respectively.
thicknesses,
are expressed
obtained
for a single
that
for one
suction-surface
tot, s, and
are
energy
quantities losses
in all channels
value,
Thus, the
suction-surface
in terms
dimensionless
of the
value, previously
boundary-layer
as
($*=
s cos a(pV)I, e,o,(pV2)i.
0* =
S COS
ot(pU2)$,
-
(7-21)
s cos a
-
O,o, 8 cos
(7-22) c_
_/ tot
_* ....
(7-23) 8 COS 8 COS
200
0t (_)(pVa)l.
a
or
BOUNDARY-LAYER LOSSES where
0*
dimensionless dimensionless
displacement momentum
dimensionless
energy
8
blade
O_
fluid flow angle
Equations tum,
(7-21),
and
energy,
ties for the These the
spacing,
equations
trailing
thickness
m; ft from
axial
(7-22), row
(7-23)
be subscripted
or station
As mentioned friction, the
kinetic-energy
to apply the
LOSS
previously,
the
and
energy
are
losses
of the
ideal
kinetic
in
terms
of
coefficient
_11a8
7-4
for the
Since
coefficient
edge,
in the
COS
dimensionless
thickness
of the
in terms
the
of the
O_la(pWa)
of
in kinetic
blade-row
actual
dimensionless
fs,la
(pV3)i,
thickness, of the
aa
(7-24)
in m or ft. trailing
la, just
surface-friction
is expressed
loss
boundary-layer
to station
only
them
as the
energy
the
region
is referenced
it represents
in terms
for evaluating
expressing
_la, defined
trailing-edge
nomenclature
this
trailing
blade-row
within
Losses
as a fraction
t is the
la,
expressed
methods
_1_= (s cos oq_--_*_s cos axe--t) where
station
will be presented.
loss
be expressed as
to be zero.
edge.
to be
and
kinetic-energy
flow, can thicknesses
quanti-
COEFFICIENTS
losses
loss coefficients
momen-
ideal
is assumed
at either
In this section,
mixing
in flow,
respective
trailing
Surface-Friction The
the losses
of their thickness
1, beyond
loss coefficients.
trailing-edge,
express
trailing-edge
BLADE-ROW
kinetic-energy
deg
as fractions
if the
can
edge,
direction,
and
respectively,
blade
thickness thickness
edge within loss.
(Refer of the
to fig. blade.)
the blade-row
If a trailing-edge
as t
t* -
(7-25) S COS
equation
(7-24)
reduces
to
ela
In order necessary
to evaluate to know
the
_la
the
--
1 -- _*_-- t*
loss coefficient
values
of the
_
(7-26) from
dimensionless
equation energy
(7-26), thickness
it is _b_* 201
TURBINE
and
DESIGN
the
either
AND
APPLICATION
dimensionless
displacement
experimentally
Experimental data
are
pressure
functions.
The
the
pressure
of (see fig. 7-1)
pressure
density
and
p,,, and
the
can be evaluated
as will be discussed
the
taken,
$1". These
determining
to measure
pressure
static
or analytically,
determination.--In
it is impractical
loss consist
thickness
experimental
and
density
data
velocity and
required
upstream
loss values,
directly.
velocity
are
pressure
loss survey
Instead, related
for computing
total
the total-pressure
herein.
the
po', the data
p0'-
friction
blade-exit P'lo for one
blade space. Since the dimensionless boundary-layer thicknesses the losses of the blade row as a fractional part of the ideal quantities could ness
pass
through
the
can be expressed
blade
row,
in terms
the
dimensionless
of the
flow
across
displacement one
blade
to
pitch
express which thickas
8
s cos ,._.(pV)i.,1o-t*s cos a,a(pV)s,,,_- cos a_of0 (pV)_odu _i*.--where (7-27)
u is the
distance
simplifies
in the
In a similar
tangential
direction,
in m or ft. Equation
to
_l_a
nesses
(7-27)
s cos _o(pV)_,,_.
manner,
=
I--t*--
the
can be expressed
dimensionless
,.
d
(7-28)
momentum
and
energy
thick-
as
01*=
(pV2)1o,1,, 1
= fo
pV
fo
V
pV
[1-(V-_f,),,]
(_),d
(7-29)
(u)
and
¢l_a --
(pf.V}.),.
pVd Assuming 202
that
the
total
temperature
T' and
the
(7-30)
static
pressure
p_, in
BOUNDARY-LAYER
the
boundary
(p/p/,)
layer
are the
l, can be related
isentropic
same
to the
as in the free
pressure
ratio
P'ljPo'
the
density
as follows:
From
the
(p_V.T
I.,1=ps,.l==po' '
and
T'I,=T_o.la=To'),
plJp/.a==plJpo ' '
division
\p--7 1_,.,.,
'
'
of equation
(7-32)
(from (7-31)
the by
ideal
gas
equation
law,
The
velocity
ratio
1,, and pl=/po'
isentropic write
relation,
(V/Vs,)la
can
with
(7-32)
-P_s,/,. - \po' ]
(p/p')
ratio
relation, p
Since
stream,
LOSSES
yields
(7-33)
be
related
to
as follows:
From
equations
(1-51)
V_ 2gJcj, T'-
T fp_C.y-_>/v 1--_-_ = 1-\_/
the
pressure
the total-temperature and
(1-52)
ratios
definition
of chapter
and
1, we can
(7-34)
where g J
conversion
constant,
1;32.17
conversion
constant,
1; 778 (ft)
Cp
specific
Subscripting values
at constant
equation
at
recalling
heat
la, that
(7-34)
dividing
the
(lbm)
(ft)/(lbf)
(lb)/Btu
pressure, once
first
(sec 2)
J/(kg)(K);
for station of these
Btu/(lb)(°R)
la and again
equations
by
for free-stream the
second,
and
P,_oa,,= Po' and T_°aa = T_= yields
pin _ (v-l)/v
1-- ---7" \Pla]
V
(7-35)
With
the
pressures
density
and velocity
by equations
equations
(7-28),
boundary-layer
(7-29),
and and
thicknesses.
can be computed The
ratios
(7-33)
kinetic-energy
from
equation
expressed (7-35),
(7-30)
Then,
the
in terms
it is now and
evaluate
kinetic-energy
of the
possible
measured
to integrate
the
dimensionless
loss
coefficient
$1=
(7-26).
loss coefficient
thus
determined
is a two-dimensional 203
TURBINE
DESIGN
coefficient; cascade order
that or from
cascade
APPLICATION
is, it is based a constant
can be, and to obtain
are taken and
AND
the
often
on data
radius is, the
full stator
a three-dimensional
at a number as shown
ary-layer
thicknesses
or rotor
radius.
obtained
by
(The
from
annular
a turbine.)
for a blade cover
boundary-layer
for each
are then
a two-dimensional
cascade.
to adequately
dimensionless
previously
from
loss coefficient
of radii sufficient
two-dimensional
calculated
either
of an annular
row,
the annulus,
thicknesses
Three-dimensional radial
In data
integration
are
boundfrom
hub
to tip:
ff'
$*_(pV)I.,I,,
cos alo r dr
h
(7-36) "' (pV)/°jo
cos al. r dr
k
cos. , r dr Ol*.a_ -
(7-37) " (pV2)f.,1,, h
cos alo r dr
d/_,,(pV 3)i.,h cos al. r dr (7-38)
_la,|D
"* (pV3)s..I.
cos al_ r dr
k
In terms
of the
measured
pressures,
these
integrals
L:i,_o(pia)i/'y[l__(P"_(_-')i'_l'l' 5"Ia,SD
expressed
as
COSalo r dr (7-39)
-_"
S,:' <,,->"'[ \p-_41
204
j
are
j
cos al. r dr
BOUNDARY-LAYER
O*a(Px_}l/v [
\po']
I_SSES
j cosaz_rdr
(7-4O) \p-_0' ]
j cos a,_ r dr
\p0']
j
cos ax, r dr
&:_,_ =
(7-41) \-_
The
three-dimensional
in a manner
similar
/
kinetic-energy to equation
j
loss
(7-26)
cos a,a r dr
coefficient
is then
obtained
: _/la,SD
_1_,3_ = 1 -- _*o.aD-- t_* where
t_* is the
trailing-edge
and is used to represent Analytical
values
lytical
methods
discussed
Center another An
average
the
for
not
methods currently
include one (ref. 2) based based on the finite difference equation
used
boundary-layer
in the
momentum
study thickness
coefficient
determined consuming
in use
values,
at the
are
solutions
are
solution. NASA
4 to
Ana-
parameters
Lewis
BoundaryResearch
on an integral method solution method of reference 3. of reference
ana-
to obtain.
boundary-layer computer
_1_ can
boundary-layer
6. The boundary-layer require
radius
row.
loss
as experimental
time
the basic
in chapter
programs
and
at the mean
for the blade
as reliable
costly
calculating
and the better
computer
value
use of analytically
less
referenced
thickness
kinetic-energy
While
are much
and
simple,
layer
with
parameters.
lytical
not
the
determination.--The
also be evaluated thickness
dimensionless
(7--42)
compute
and
turbulent
was
0.231 01a
_---
,
×
\_ccrlfa,
la
(7-43)
205
TURBINE
DESIGN
AND
APPLICATION
where parameter
defined
X
distance
l
blade-surface
along
by equation
blade
(7-15)
surface
distance
from
from
forward
forward
stagnation
to
rear
point,
m; ft
stagnation
point,
m; ft viscosity, The
(N)
development
sumed
that
reference
(sec)/m_;
of this
the
equation
boundary
4, the
lb/(ft)
is presented
layer
exponent
has
n was
,
(7-43)
surfaces
of the
equktions
blade.
(7-43)
blade-surface channel
and
factor
from
for
the
parameters from stator from
thickness
for the
ably
close
tained from
blade
the computer
programs
from
parameters
would
sufficient have
to be
reference
shown
In (1) by
206
the The
the
losses good
over
is commonly with
of reference
used.
as
were
reason-
results
ob-
obtained
be
calculated thickness
at a number length
and surfaces.
simplified from
obtained
of radii
would
also
Such method
two-dimensional by this
method
results.
5, the
following blade
thickness
values, momentum
could
losses
loss for the
momentum
the
3.
end-wall
Results
be
For
as those
so the
experimental
known
$_ can
however,
blade
the
can be
chapter.
two-dimensional
effort,
of the
boundary-layer
analytical
determined
three-dimensional
momentum
dimensionless
The the
surface
individually
2 and
over
considerable
agreement
method average
variation somehow,
require
5 for predicting
mean-section have
determined,
would
the
parameters
to (7-38).
and
coefficient
In general,
to be analytically the
various
be as accurate
of references
of the
any
boundary-layer
surfaces
not
to the
by (7-43)
in this
4,
for
5.
loss
the
required
01a, Hla, and E_
earlier
two
will
(7-36)
have
to establish
procedure
the
pressure
adjacent
la for each
surfaces,
boundary-layer
equations
values
With
values.
(7--43)
densities
(7-14).
of
for the
experimental
equation
Three-dimensional directly
and
and
in equation
in reference (7-43),
and
obtained
kinetic-energy
studied
suction
in chapter
presented
equation
to the
from
the
equations
blade
calculated
pressure
the
be
Ela at station and
In
equation
(7-44)
free-stream can
is as-
profile.
referenced
1
both
discussed
4. It
velocity
the
velocities
those
factor
and
the
for
These
(7-13) and
xj
H as required
energy
suction
evaluated turbine
factor
equations
thickness
are
layers. techniques
Hla and
obtained
evaluated
(7-44)
form
from
L\-_-Iy.
free-stream
boundary of the
both
be
The
flow analysis
Values form
must
in reference
a power-law
obtained
n Equation
(sec)
assumptions surface
at
the
are
made:
can be represented blade
mean
section;
a of
BOUNDARY-LAYER
LOSSES-
Approximate area o{one end wall
sccosas)7
t
Approximate
F/:iiii::iilfi:,i::iiiiiii::::i::ili::f|iiiiii::iiiil direction [ ]!{i]_[i] []]]_]]]_][:i]i[]i][][ ]]]]]]]][]i]i ][_ _]]i]i]_]![i]i]i !1
s_de of blade
__:_;_i_;;_i_!_i_ _I_i_::_]_;_ :::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::×
:::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::::: ::i:::::::::::::::::::::::::::: :':':"::_i_''"' •
" "::::_!:i:i:_:
============================= .....
_%%_,_. •
::::::::::::::::::::::::::::
•
_''"
_
I------ s-----
FIGURE
7-5.--Schematic
diagram the effect
late
(2)
the
momentum
the same and
(3)
stant
the
blade
cross
section
loss per unit
as the average
equivalent
of equivalent of end-wall
area
momentum
configuration
can blade,
section,
and
spacing,
given
(see fig. 7-5)
blade.
on the
inner
loss per unit
two-dimensional of the
two-dimensional area on blade loss.
stagger
outer
end
7-5,
equal
to those
area
to
of one
calcu-
walls
is
surface;
approximated
in figure
angle
surface
used
on the blade
be satisfactorily as shown
The
and
area
blade
by an
having at the
equivalent
a conmean blade
is Ab = 2ch
(7-45)
where Ab
total
surface
areas) C
blade
chord,
h
blade
height,
The
inner
and
area
(sum
of one blade,
outer
of suction-surface
and
pressure-surface
m_; ft 2
m; ft m; ft end-wall
area
for one passage
Aw=2sc
is
cos a,
(7-46)
where Aw
total
surface
end-wall blade Now,
taking
stagger
area
of passage
areas), angle,
the average
end
walls
(sum
of inner
and
outer
m2; ft _ deg
momentum
loss O'a.,,, over
the blade
radial
length
207
TURBINE
and
DESIGN
modifying
AND
APPLICATION
it to include
the
01"3D=0" The
calculated
losses
yields
fAb-t-Aw_-O*
three-dimensional
are then
end-wall
energy
and
(1_
sc°sa')
displacement
(7-47)
thickness
parameters
as * _la,3D
_
* ,mOla,3
Ela
(7-48)
D
and 5"la,3D = Hla , m01*o , 3D Mean-section the
values
energy
and form
boundary-layer
factors
used
dimensional
for the
were
thicknesses,
satisfactorily tion
are used
energy
as is done
and
originally
(7-48)
coefficient
factors.
in terms
in reference
in equations loss
form
defined
it is indicated
kinetic-energy
(7-49)
of individual
4 that
and
is then
Although they
(7-49).
obtained
can be
The
three-
from
equa-
(7-42). Trailing-Edge
The with
kinetic-energy flow
past
mentally
loss coefficient
the
blade
_te that
trailing
edge
represents
can
be
the loss associated
determined
either
experi-
or analytically.
Experimental
determination.--Experimental
edge loss coefficient _te are obtained two-dimensional loss coefficients loss and blade
Loss
trailing-edge
loss, and
surface-friction
values
from differences _1, which include
loss coefficients
of blade
trailing-
between experimental both surface-friction
_1_, which
include
only
loss. Thus,
e,e= :1- e_. Loss
coefficients
_1_, which
tained as described surface-friction
loss and
on data
where
the
the
obtained
which
measurements
blade
include must
little
Analytical
mixing,
:1, which
include
obboth are were
not
determined
are
the
the
are
loss,
in exactly
blade
yet
trailing
occurred.
surface-friction
be made
at
to station
edge
To
determine
loss and
a location
1 in figure
just
at station the
trailing-edge downstream
7-1, where
la, loss loss,
of the
the trailing-edge
has occurred.
determination.--In
are
presented
for a large
the
reference
are
208
coefficients loss,
within
both
surface-friction
total-pressure loss and static pressure The surface-friction loss coefficients
loss has
row, corresponding
loss, but
trailing-edge
just
(7-50)
only
Loss
that the locations.
trailing-edge
coefficients
include
previously.
same manner except measured at different based
the
reference number
experimental
6, experimental
of surface data
for
drag
discontinuities.
sheet-metal
joints
coefficients Included of different
in
BOUNDARY-LAYER
LOSSES
T ¥I
_u11
FIGURE
geometry, edges.
bolt
7-6.--Schematic
and
rivet
It is indicated
behaves
similarly
Therefore,
the
lytically
diagram
heads
that
of different
the
regardless loss due
of the
and to the
a trailing
to a body
layer.
loss due
flow direction
past
due
in boundary
geometry,
pressure-drag
to flow
as if the loss were
of body
over edge
placed
the
airfoil
trailing
discontinuity discontinuity.
will be treated
in the
path
ana-
of a boundary
layer. As indicated
in reference
to or less
than
boundary
layer,
effective height
the
6, the
drag
full boundary-layer
as shown
dynamic
pressure
of the body.
Thus,
in figure of the
of a small height
7-6, part
body
6y=u, placed
corresponds of the
of height
h, equal
in a turbulent
approximately
to the
layer
to the
boundary
equal
D = q_IihCD
(7-51)
where D
drag
h
height
on body,
drag and
the
of body,
N/m;
lb/ft
m; ft
coefficient
effective
dynamic
pressure
qell=h
Drag
is related
to momentum
q_f_ is expressed
J o
thickness
2g
as (7-52)
dY
as
D= O(pV_)I° g Therefore,
a
trailing-edge with
a properly
dimensionless loss is obtained subscripted
momentum by form
combining of equation
(7-53)
thickness
e*,
equations (7-22)
representing (7-51)
and
the (7-53)
: 209
TURBINE
DESIGN
AND
APPLICATION
q,LrhCo
8",-
(7-54) (pV2)fs 8 COS 0_1 --
g The
flow angle
(4-26)
and
Before sure the
a, is related
to the
angle
ala as discussed
must
(7-54)
be determined.
free-stream
dynamic
can
be evaluated,
The
ratio
pressure
the
of the
is equal
turbulent with
Combining
flow,
the
the
use
equations
effective
effective
dynamic
dynamic
pressure
that
the
layer
and
free
stream
dr
variation
of velocity
of the (7-8)
tion
(1-64)
total
simple
and
(7-55)
in the
power
(7-12)
boundary
profile
layer
presented
of chapter
the
can be
previously.
yields
(7-56)
temperature
are
to
h
V/. Assuming
pres-
to
-
expressed
4 (eqs.
(4-27)).
equation
ql, For
in chapter
and
same
and
static
using
pressure the
ideal
in the
boundary
gas law and
equa-
1 gives
To'
7+ I
_
I, (7-57)
P/*
To' Substituting the parameter
equations
(7-56)
A _, defined
"y+ 1 and
1-
Performing qy!=(l_A/, qy,
a binomial
(7-57)
by equation
expansion
and
in equation
(7-15)
A
fs
and
using
\_u/l/
integrating
then
gives
) [( h ) 2" 1 ( h _4'_ A,. L\ (i/,, ,z/ 2 n -l---_l-I- k _. zt/ (4n+l)
(h_y + \(_f.../ 210
(7-55)
yields
_ (6n+l) A_
+.--
]
(7-59)
BOUNDARY-LAYER
Substituting
equation
thickness
t in place
(7-59) of body
tCD (l_As,) 2s cos a_
0"-
in equation height
(7-54)
h finally
L\_-_-!
_,
(4n+
+ The
boundary-layer
be the
thickness
sum of the
Equation
suction-
(7-60)
n is not
well
incompressible
the
flow
and
n=l/_
(7-60)
(7-60)
should
values.
flow.
following
+""
in equation
pressure-surface
is for compressible
known,
trailing-edge
1)
(6n+l)
_f_u to be used
and
using
yields
+
2n+l
and
LOSSES
In many
simplified
cases,
equation,
(commonly
used
at least which
for
when
assumes
turbulent
flow),
is adequate: 0",=0.375_The information be set
equal
trailing verted edge
in reference to 0.16
edge.
The
0.22
basis
for
will be available.
ted S COS oq
6 indicates
a rounded
corresponding
to the same and
for
t _futZ
trailing values
as equation
a square In such
that
a case,
the
drag
edge
and
reported
(7-61)
trailing
(7-61) coefficient 0.22
C9 can
for
in reference
a square
7 and
are 0.14 for a rounded
edge.
Frequently,
for incompressible
con-
trailing
5to, instead
of _i/_,
flow, (7-62)
and
for compressible
6full
flow, (7-63)
--
1-
Equations momentum
(7-60) due
kinetic-energy
the
(7-61) blade
loss coefficient,
evaluated
flow and from used to obtain
and
to
in flow and kinetic factors,
(1 -- Ay.)
energy. from
equations
1 , (n--_-t-_
give
trailing
the edge.
it is necessary
As a simple equations (7-16)
A/.
A_, t 5-_-t-
(7-17)
5*, = He*,
, • • ")
fractional To
find
to find
approximation, (7-13)
and
,
and
loss the the
in
corresponding fractional
the form (7-14)
blade-row
for
for incompressible
losses
and
energy
compressible flow,
are
(7-64)
and d/*, = EO*,
( 7-65 ) 211
TURBINE
DESIGN
At station flowed
AND
1, which
into
the
APPLICATION
is just
downstream
area behind
due to trailing-edge is obtained as
the
blockage.
of the
trailing
blade
edge
Therefore,
trailing
and there
edge,
fluid has
is no longer
a kinetic-energy
loss coefficient
* This
loss coefficient
ideal
kinetic
were
the
energy
only values
thickness.
This
energy the
The
surface-friction
would
flow
associated
loss
is approximately, coefficient.
and trailing-edge loss in terms cussed in the next section.
as a fraction
if the
trailing-edge
on
loss
exist
of trailing-edge
(7-66).
energy
kinetic-energy
against
is based
in equation
loss coefficient
that
trailing-edge
of the ratio figure
(7-61).
included
flow
flow is plotted
for several
not
The
(7-66)
the loss in kinetic
of the
loss.
incompressible
equation
expresses
the
a void
trailing-edge loss
thickness with
Therefore, but
as expressed
blade-surface
not rigorously,
Expression
7-7
of the
by
friction
trailing-edge
of a kinetic-energy
for
in figure
to boundary-layer loss
this
loss
coefficient
thickness
momentum
of the
additive
combined
is
kineticwith friction
loss coefficient
is dis-
Ratio of trailing-edge thickness to boundary-layer height,
. O2O
U_ul; 1.O i
.015 .5
_
.olo .!
_
.005
0
.05
.10
.D
Dimensionlesstrailing-edge thickness, t*
FIGURE 7-7.--Effect of trailing-edge blockage on kinetic-energy factor H--1.3; energy factor E-1.8; drag coefficient
212
loss coefficient. Cv--0.16.
Form
BOUNDARY-LAYER
Combined As stated
in the
Friction
discussion
thickness
parameters
combined
friction
and and
and
of the
Trailing-Edge
trailing-edge
a kinetic-energy
trailing-edge at
a location
which
downstream
of the
trailing
experimental versions obtained
values
of &*, 01", and
of equations as
(7-28),
Analytically, Before
adding
the friction
can be added, The
must
in terms
ever,
there
with
blockage
there
is no blockage.
must
parameters are flow as follows:
adjusted
to
the
subscripted of _1 is then
la
trailing-edge la,
ideal
friction-loss for
at station
the
sCOS c°s Ola--t al"
ideal 01*a,
flow.
_l*a) are
blockage. the
(with
How-
ideal
at station
boundary-layer true
loss.
parameters
(61",
where
flow
1 are
trailing-edge
thickness
at station to the
to account
1,
we obtain
of the same
at station
flow without
the
station
way,
parameters
on the basis
blockage
Therefore,
the
The value
boundary-layer
be comparable
by making
appropriately
loss
thicknesses
of an ideal
the
(7-67)
thickness
be expressed
is a trailing-edge
expressing to
In this
(7-30).
surface-friction
dimensionless
boundary-layer
1--61"
and trailing-edge
they
friction-loss
expressed
the
edge.
and
the boundary-layer
by
the
corresponding
_1" from
(7-29),
-
obtained
loss,
loss can be obtained
measurements
is just
Los
loss coefficient
experimental
LOSSES
flow
1, where thickness
blockage)
)
ideal
_*1,/_
_*(s la
(7-68)
0*
0* (s sc°sal"
(7-69)
, = _bx_ ,( s scosa_ _bl'! cos al_-- t )
(7-70)
and
where
the
friction parameters
subscript
and
f refers
trailing-edge at station
to the loss due
to surface
loss parameters
then
friction.
yields
the
Adding combined
the loss
1: 6x* = _I.IA-_ t.
(7-71)
01" = Ox,/A-O t,
(7-72)
and _ll*
And
the value
of _1 is then
obtained
--
IY l,f
from
(7-73)
'fire
equation
(7-67). 213
TURBINE
DESIGN
AND
APPLICATION
After-Mix The
after-mix
loss is the total
the trailing-edge $2 is determined is obtained
loss, and as described
pressure plete
the
the
has
includes
previously
after-mix
measurements mixing
loss that
the
surface-friction
the mixing loss. The after-mix in this section, and the mixing
by subtracting
To determine
Loss
determined
loss experimentally
be made
occurred.
downstream
This
loss coefficient loss, if desired,
_1 from would
of the
is impractical
$_.
require
blading
for
loss,
that
where
several
mixed, that
length,
thus
values
of after-mix
the
these use
leading
possibility
reasons, of
error;
po'-p2'
would
of measurement
error
values
either
(station
to possible
of after-mix
experimentally
would
analytically
and
axial
momentum
flow rate
before
in the mixing
conservation
f0 from
(pV2)l
these
in the
small
enough
large.
analytically
are
For
with
the
before-mix
in the
and
could flow
were
before-mix
station
is not
station
direction
a2 cos a_(pV2)_ axial
direction
(7-75) we get
_ a2(oV2)_
for two-dimensional at station
evaluated conservation
1, it would
mass
we get
flow by integrating
These
the
2) yields
(7-74)
= gp_+cos
available
be directly angle.
Equating (station
a2(pV)2
tangential
subscripted
data
mixing. mixing
written for any before-mix location at which data used to evaluate the after-mix loss coefficient.
214
flow had
after-mix conditions are in the tangential direction,
=cos
=sin
to three-dimensional survey
equations
pressure
d
(oV 2) cos 2 al d
equations
also be applied above
o1
of momentum
+
If experimental static
cos
after
sin al cos al d
conservation
'
the
and
determined
the
during
1) and
of momentum
g fo p_ d Although
direction
(station
o(pV)1
can
the
1) loss parameters. for determining of mass, momentum
and
(1)
(2) the for the
after
be relatively
obtained
The basic equations those for conservation
From
(3)
be constant
loss are or
and
com-
reasons:
The length for complete mixing, while quite long, is unknown; after-mix loss would have to be corrected for side-wall friction mixing
the
even
(7-76) flow,
they
radially. 1, the
with
integrals variations
equations
could
were available, In the case
not be possible
in in be
and then where the
to determine
BOUNDARY-LAYER
the
mixing
ever,
loss completely
it is only the
ments
are usually
where
angle
possible used
to express
herein
differs
used
farther
that
for
station
l,
to (7-76) 1 only
where
there
(pV)ld
in that la
is no
measure-
trailing station
for station
of the
previously
1. The
analysis
the
before-mix
station
herein.
Equation
(7-28)
trailing-edge
I and
edge, 1, it is
void,
=(1--Sl*)(pV)l.a
(7-29)
can
be
(7-77)
combining
it with
equation
yields
(pV2)l Substituting (7-76)
d
equations
yields
momentum mined:
the
= (1-8,*-01")
(7-77)
and
following
in terms
gpl+cos
(pV2)ioa=cos
equations,
along
with
the
ideal
equation
(TI'=
T_'),
can
be
1 to
for both
cos
(pV2)s0a
energy
obtain
_,
compressible
and
incompressible
flow,
the
gas
after-mix solution
(7-74) of
_ a2(pV2)_Wgp_ and
and deter-
(7-80) (7-81)
the
conservation-of-
simultaneously
as shown
kinetic-energy
to
(7-79)
a2(pV)2
law
mass
previously
= sin a_ cos a_(pV2)_
solved
incompressible the
equations
parameters
sin al cos al(1 --81"--01") 2 al(1-81"-01")
(7-78)
conservation
(pV)f,,1--
These reference
into
for
boundary-layer
oq(1--81")
(pY_)l..l
(7-78)
equations
of the COS
For
across in terms
how-
out.
in reference
to station
1
equation
of the
constant
cases,
survey
damped
as was done
of reference
and
somewhat
are
(7-74)
In most
downstream
have
angle
1 corresponds
fo
(7-77)
is desired,
parameters,
from
Subscripting
flow
equations
in reference
subscripted written as
loss that
variations
and
boundary-layer
means.
a little
pressure
pressure
experimental
after-mix
made
and
If static
final
by
LOSSES
loss
in
coefficient,
flow. for _2 is
)+co 2
sin 2 al (1 - _l*-- 01"\ _ _2=1--
(7-82) 1+2
For steps
compressible are required
flow,
COS 20t1[-(1--_1*)
no explicit
to obtain
solution
2-
(]--81*--01*)_
was
found,
and
the
following
_:
215
TURBINE
(1)
DESIGN
AND
The parameters
APPLICATION
C and D are computed
?+1 --_-7 +cos_
(1--As.a)
from
(V)' _
at(X--*t*-01*)
y.,t
C-
(7-83)
D
(2)
The quantity
V =(V-f_,)t,,tsinal\
(V,/Vc,)2
The
density
ratio
is obtained
(o/p'):
The total
pressure
from
is obtained
(_)---_1 (4)
(7-84)
/
(7-s5)
.yC X/(.yC )'_l+(.y-1)D, ,+1 - 7-4-i / 7-;il
(___,.)_ (3)
(l-_x*-0,*_ ]_-_1"
('),-I'_[-
ratio
i0_I
from
p2'/po'
P
c,
(7-86)
,V_, \:]'I''('-')
is obtained
from
j.,_.-7_., cos _x(1- _,*) (7-87)
,o, \O
(5)
The
pressure
ratio
(p/p')_
is obtained p
(6)
Finally,
_2 is obtained
gc,l_
from
p
v
(7-8s)
from
(7-89) (p,'_(',-"/, -\pi
Values the
216
blade
of _ include row,
the
all the blade-row trailing-edge
1
/
loss,
loss; and
that the
is, the frictional
mixing
loss.
Values
loss of of $1
BOUNDARY-LAYER
include
all the
blade-row
losses
except
mixing
LOSSES
loss. Therefore,
_miz = &-- _ where
_m;z is the
fractional
loss in available
BLADE-ROW In
this
the
section,
various
effect
LOSS
types
will
geometry
7-8,
analytically
angle
senting
at the the
losses. edge,
(arithmetic
edge,
section;
annulus
The
including
the
stator
the
and
experimentally loss coefficients
and
at
three
the
the the
friction
end-wall
between good.
_1._,
at three
at
repre-
within
friction,
mean
obtained
just
the
total
tra_ling-edge
experimental
the
the
loss plus trailing-edge
_2.3D represents the
just
loss
coefficient
and
stations
$1,.m, obtained
surface-friction
coefficient and
mixing. In general, agreement loss coefficients is reasonably
0
compares
of kinetic-energy
represents
blade
.04 __
8,
section;
and
compared,
of
of Losses
loss coefficient
radius)
the trailing
Comparison
a given
represents
mean
mean
for
and
losses
will be discussed
reference
values
settings
different trailing
beyond
from
determined
be presented
and
determined
different blade
taken
due to mixing.
analytically
on losses
Distribution Figure
and
considered
energy
CHARACTERISTICS
experimentally
of blade-row
(7-90)
and
loss loss for
drag,
and
analytical
Experimental results
t'3 Analyticalresults O_"
e2.3D"
.0:
!
Mixing and end-v/all losses
Trailing-
edgeloss g_ ¢-
ela. m
?
t_
Mean-section blade suf/ace friction loss
.0: ¢,m v
o 70
I
I
100
Do
Percentstatorareasetting
FIOURE 7-8.--Comparison
of experimental stator
area
settings.
and analytical (Data
from
loss coefficients for different ref. 8.)
217
TURBINE
DESIGN
AND
APPLICATION
A el,30 .05
0 el, m 0 ela, m
,o ,Mixinq loss End-wall loss
¢,.
Bladesurface friction loss
.01 --
o
I
I
.5
.6
.7
I ....
I
.8
.9
Mean-section ideal after-mix critical velocity, (VNcr)i, m, 2 FIGURE 7-9.--Variation
Figure row,
but
7-8
gives
does
of loss coefficients
some
not
from
reference
locity.
Loss coefficient
In this particular loss was
about
loss
will
The
end-wall
case,
the
vary
is seen
The
case,
The
one-quarter with
the
friction of the
was
the
design,
does
will,
total
total
stator
loss.
as was
15 percent
of course,
vary
indicate
that
each
velocity.
losses,
as well
of the
trailing-edge
the
in figure
total on radius
the
stator
losses
stator
trailing-edge
10 percent
of the
ve-
2 percent
shown
with
7-9,
loss. The
primarily
remaining
Figure
increasing
of the
up the
blade
with
In general,
blockage depending
in a stator
end-wall
loss was about
ref. 9.)
coefficient
with
and
from
losses.
in loss
mixing
about
loss made
loss breakdown
end-wall
slightly
of the
trailing-edge
with
and
the
(Data
of losses
variation
to decrease
which
mixing
comparison
mixing
one-half
velocity.
distribution
the
separately losses.
about
loss,
will vary
spacing. loss.
and
the
9, shows
This figure also shows as the other blade-row energy
of the
separate
taken
ideal
idea
with
may
7-7.
loss for this ratio
and
of the
total
design, be
of
but con-
sequence. Effect A study layer 218
of the
of Blade-Row
effect
loss is presented
of turbine in reference
Geometry geometry 10. In that
on Losses
on turbulent-flow study,
the
boundary-
assumption
was
BOUNDARY-LAYER
made
that
the momentum
of the chord
Reynolds
loss per unit number
blade
surface
LOSSES
varies
as the
inverse
to the m power:
--_Re7
_
(7-91)
C
where
Rec
equation into
is
a Reynolds
(7-91)
number
based
by multiplying
equation
(7-22),
three-dimensional
and
effect
and
then
0,*¢¢ (_)m
chord
c. Expanding
by like terms,
equation
an equation
_1 +cos
blade
dividing
using
yielded
on
(7-47)
substituting to express
the
of the form
a._ (O,ot_
(7-92)
(_)1-_Re__,,,
fC.),(",,) where the
Reh is a Reynolds
number
three-dimensional
as
a function
blade given
c/s,
(there values
minimum
from
reference
each
figure
change
analysis. of the
values
of the
results
from
number
nature
shows the the
and
be varied
loss.
Comparison
a wide
optimum
causes
two
shape
chord
Reynolds
The
7-10,
was
and
thickin
of the other With the loss around
of the
7-12.
variation
ex-
obtained
in terms
results
7-11,
geometry variation little
counteracting area.
considerably of the
sensitive
curve
momentum
variable
determined.
in figures of the
that
end-wall
may
loss is more
then
The
a
analysis
Also shown
associated
with
in the
variable.
7-10
around
were
value
loss for
of solidity.
variables
of each
h/s,
reference
minimum
dimensionless
geometric
value
10 are shown is the
value
be expressed ratio
Reh. The on the
a function
derivative to each
can
is no minimum for height Reynolds number). known, the relative variations in momentum
in each
Figure
number
becomes
to find the minimum-loss
variables optimum the
respect
h. As indicated,
parameter
9, is based
to _/_ in the
10, the
08* with
Reynolds
therefore,
m is set equal
order
height
height
variables--height-to-spacing
in reference
and,
In reference hess
and
on blade
thickness
geometric
as explained
solidity
ponent
momentum
of the
solidity
of O,,,/c,
based
of figure number
7-11
from
to solidity 7-11 and
increase
effects
Figure
results
(50
optimum than
reflects end-wall
with
to the also
that
7-10 the
or more)
in momentum
of changes
shows
in figures
percent
loss.
This
in chord
Reynolds
solidity
of a blade
but
excessive,
the
some, and
in h/s
7-11
height-to-spacing counteracting
not shows
that ratio.
influences
the The of
area. 219
TURBINE
DESIGN
AND
APPLICATION
/_
_/////_/////// I
! I I
i
I
/ H n
,;7 .=L4-
J/,4
E._I 1.21-_'--,==P
I \
==o-
¢/s and Reh are constant
IX, .2
.6
LO
L4
2.2
1.8
Z6
Height-to-spacing ratio relative to optimum ratio, (htslllhlslopt FIGURE 7-10.--Variation
of momentum-thickness ratio with spacing ratio. (Data from ref. 10.)
variation
in he_ht-t_
_<'//////////(/ I I I I
Y/'//////
///i
_ I
,/
b;'/ _:,,, j', J" _i/I-
= .=_ i. 4o . \ _'_Z_ _
his and Reh are co
Lo
I
t"--_ I _
.4
.6
.8
LO
1.2
I
J
1.4
1.6
Solidity ratio, (cls)/(c/s)opt
FIGURE 7-11.--Variation
220
of momentum-thickness from ref. 10.)
ratio
with
solidity
ratio.
(Data
BOUNDARY-LAYER
LOSSEF
t //.
/////Z I ! I
1
_Ls -
1.6
_
1.4
/
.,
4 //[
his and c/s areconstant
.s
I ._
o
I .4
I .6
I .s
I Lo
I _2
I
I
].4
L6
I--7 L8
2.0
HeightReynolds numberratio, RehlReh,ref FIGURE 7-12.--Variation
Figure height
7-12
shows
Reynolds
Reynolds
could
the
variation
number
number
number
of momentum-thickness ratio with height Reynolds number ratio. (Data from ref. 10.)
due
ratio.
While
to change
also result
from
in height
Reynolds
figure
indicates the
in inlet
ratio
results
change
is sometimes
used
The
curve to the an in-
performance.
in correlating
the
in
in Reynolds
flow conditions.
in improved
with
a change
loss being inversely proportional power. These results show that
number
height Reynolds number of different turbomachines.
the
in geometry,
change
shape, then, results from the Reynolds number to the m=_ crease
of momentum-thickness
The
performance
REFERENCES 1.
STEWART,
L.:
WARNER,
Characteristics Boundary-Layer 2.
McNALLY, NASA
3.
PATANKAR, Layers.
4.
WHITNEY, mental acteristics
of of
and TN
l).:
S. V.; CRC
TN
3515,
Program
Boundary
AND SPALDING,
WARREN
Compressible-Flow Blade
Layers
Loss
in Terms
of
Basic
1955. for
in
Rows
Calculating
Arbitrary
Compressible
Pressure
Gradients.
1970.
Press,
Investigation and
NACA
FORTRAN
Turbulent
D-5681,
Two-Dimensional
Turbomachine
Characteristics.
WZLLIAM
Laminar
Analysis
Downstream
D.
B.:
Heat
and
Mass
Transfer
in
Boundary
1967. J.;
STEWART, of
WARNER
Turbine
a Comparison
with
L.;
AND
MISER,
Stator-Blade-Outlet Theoretical
JAMES
W.:
Boundary-Layer Results.
NACA
RM
ExperiCharE55K24,
1956.
221
TURBINE
5.
6.
DESIGN
STEWART,
WARNER
WHITNEY,
Turbine
Losses.
Stator
HOERNER,
SIGHARD
HERMAN and
NASA
Cooling.
TM
X-1696,
Variable
the
AND WONG, in
E,55L12a,
Y.:
Use
of
Three-Dimensional
1956.
Drag.
Midland
RONALD
Performance
ROBERT
Predicting
Park,
M. : Effect of
Certain
N.J.,
1965.
of Trailing-Edge Turbine
Geom-
Stator
Bla_ling.
MOFFITT, on
THOMAS
Performance Detailed
P.; of
Losses
AND
BIDER,
a Single-Stage with
70-Percent
BERNARD: Turbine Design
Effect Suitable
Area.
of for
NASA
1968. P.; PRUST,
Stator
Area
on
II--Stator
X-1635,
HERMAN
W., JR.; AND
Performance Detailed
of
Losses
BIDER,
a Single-Stage with
130-Percent
BERNARD: Turbine
Effect of
Suitable
Design
Area.
WARREN
J.:
for NASA
1968.
JAMES
of
Turbomachine RM
RM
AND HELON,
V--Stator
MISER, NACA
J.;
1972. Area
THOMAS
Air Cooling.
NACA
on
W.;
Stator
WARREN Parameters
Fluid-Dynamic
JR.;
D-6637,
Air
TM
W.,
HERMAN
9. MOFFITT,
F.:
Thickness
TN
PRUST,
Variable
222
L.;
Boundary-Layer
etry
10.
APPLICATION
Mean-Section
7. PRUST,
8.
AND
W.;
STEWART,
E56F21,
Viscous 1956.
WARNER Losses
L.] Affected
AND WHITNEY, by
Changes
in
Blade
Analysis
Geometry.
BOUNDARY-LAYER
LOSSES
SYMBOLS
Ab
surface
area of one blade,
,41,
parameter
A. C
surface
defined
area
parameter drag
by equation
of end
walls
defined
(7-15)
for one passage,
by equation
m2; ft _
(7-83)
coefficient
C
blade
Cp
specific
D
drag, N/m; lb/ft parameter defined energy factor
E
m2; ft 2
chord,
m; ft
heat
at constant
kinetic-energy
pressure,
J/(kg)
by equation
(K) ; Btu/(lb)
(°R)
(7-84)
loss coefficient
g H
conversion form factor
constant,
h J
blade height, m; ft height of body placed in boundary layer, conversion constant, 1 ; 778 (ft) (lb)/Btu
l
blade
m
exponent
n
turbulent
P
absolute
pressure,
N/m2;
lb/ft _
q Re_
dynamic
pressure,
N/m_;
lb/ft
Reh
height
r
radius,
m; ft
8
blade
spacing,
T
absolute
t
trailing-edge
U
distance
V
fluid
X
distance
Y
distance
Y
distance
surface
1; 32.17
distance
(lbm)
from
(ft)/(lbf)
forward
(sec _)
m; ft to rear
stagnation
point,
m; ft
chord
in equation
(7-91)
boundary-layer
Reynolds
velocity
profile
exponent
2
number
Reynolds
number m; ft
temperature,
K; °R
thickness, in tangential
velocity,
direction,
m/sec;
along
m; ft m; ft
ft/sec
blade
surface
from
forward
stagnation
point,
m; ft from
surface
from
fraction
normal
surface
to boundary
normal
of boundary-layer
(x
fluid flow angle
o_m
blade
stagger
3_
ratio
of specific
constant
from angle
heat
boundary
m; ft
layer
expressed
as
thickness
axial from
to
layer,
direction, axial
at
deg
direction,
constant
deg
pressure
to
specific
heat
at
volume
boundary-layer
displacement
boundary-layer
thickness,
thickness,
m; ft
m; ft
223
TURBINE
0
DESIGN
AND
boundary-layer viscosity,
P
APPLICATION
density,
momentum
(N)
(see)/m2;
kg/m3;
thickness, lb/(ft)
(sec)
lb/ft 3
boundary-layer
energy
thickness,
m; ft
Subscripts: cr
critical
flow conditions
eft
effective
f
friction
fs h
free hub
i
ideal
inc m
incompressible mean section
min
minimum
mix
mixing
opt
optimum
stream
p
pressure
ref s
reference suction surface
surface
t
tip
te tot
trailing total
x 0
axial component blade-row inlet
1
just
la 2
just within downstream
3D
three
edge
beyond
trailing
Superscripts: absolute
*
dimensionless
224
of blade
trailing edge of blade uniform state
dimensional
t
edge
total
state value
row row
m ; ft
CHAPTER 8
Miscellaneous Losses By Richard J. Roelke In the
last
process
chapter,
in the
design-point include
these
losses
neglected;
of
in other
part
instances,
comprises
losses
turbine
these
losses
turbine
all the
losses
turbine.
turbine
considered,
there
is being The
blade
partial-admission
inactive
passages
blade
as they
a loss that
occurs
at off-design
loss, which
will also be covered
pass
of the the
a turbine
rotor
tips,
blades
thus
amount
shrouds. the
reaction)
first
causes
since more
casing,
nature by
geometry, a large
some
some
point.
be
mag-
The
sum in the
a partiallosses
considered
the
that
are the
filling-and-emptying
admission turbine
clearance
fraction
in turbine
clearance, tip
be of such
additional
the
may
arc. Finally,
is the
incidence
LOSS
with
a reduction
a given loss,
operate
the
and
herein.
of all, by the
of radial
For
leakage
and
causing
loss is affected, the
must
instances,
however,
usually
of any
flow
overall
are considered
are and
TIP-CLEARANCE Because
can design
If,
through
operation
In some output
that
losses channels
the
the
also be considered;
loss.
of the
of the
with
determine
must
disk-friction
axial-flow
loss in the
loss in the
other
the selection
normally
associated To
a full-admission
be included.
pumping
small
losses
discussed.
loss and
a very
however,
admission must
represent
losses
design
were
of a turbine,
tip-clearance
as to influence
of these
boundary-layer
channel
efficiency
these
nitude
the
blade
pressure
higher-kinetic-energy
of the
work
of the
recesses the
between
tip in
amount difference
the
fluid
output.
leaks This
geometry;
across
flow to leak
and
reaction the through
tips
across leakage
that
casing,
of blade
the
is, by by
tip
affects tip
(high the
tip 225
TURBINE
DESIGN
gap
the
from
shrouded
but
problem. developed,
flow
not
side of the
only
causes
rather
of the
in turbine
drop
difficult
of tests
to determine
the
and tests
loss. Figure
have
effect
reaction helps 8-1
and been
made
of tip
because
shows
the
60
and
that
caused
complex
none
flow
of some
at the blade
on of the
of the exit
is entirely
Research
geometry
understanding
traces
things space
own in the
efficiency
Lewis
tip
An examination
angle
stage turbine (ref. 2). Two that the flow in the clearance
to its
primarily
of the
states
at the NASA
a better
an un-
clearance loss have been in reference 1; however,
author
clearance
turbines.
to obtain
the
With
a loss due
of the blade,
is inherently
complicated,
blade.
an unloading
evaluation
leakage
satisfactory. A number
these
suction
Several empirical expressions for and some of these are summarized
are
impulse
leakage
also causes
Analytical
by tip-clearance
they
side to the
this
work,
region.
APPLICATION
pressure
blade,
reduced tip
AND
Center axial-flow results
of
tip-clearance
of a 5-inch
single-
to be noted from the angle traces are and near the tip was not fully turned,
Tip clearance, percent of passage height
4_
2'
2O
0
1 2
1:3
•
5.0
o
8.0
Axial
,,
direction =
-6 4--P
-2O
-4C .5
FIGURE
8-1.--Variation
lTr +,,I .6
of exit
I
.7 .8 Ratioof hubradiusto tip radius
flow
angle
(Data
226
I
with from
radius ref.
2.)
ratio
Oo,+rw.,, I,
.9
for four
1.0
rotor
tip clearances.
MISCELLANEOUS
LOSSES
Turbine 0 C] Z_
1-Stage,reactionIref. 2) 2-Stage,reaction(ref. 3) l-Stage, impulse(ref. 4)
--Estimate (ref. 5) for ref. 2 turbine m m Estimate (ref. 5)for ref. 4 turbine 1.00
m
.96 _
\\
.80
I
.76' 0
FIGURE
even
at the
increased way
down
to the
hub.
in figure The (ref.
the
2) and
results
in figure
I
I ,12
on efficiency.
tested,
and that
underturning
clearance,
and
effect
in lower turbine,
4).
this
of the
flow
of the flow
occurred unloads
turbine
output
as well
as for two
of reaction the same
lines
and
Extrapolation
of the
satisfactory
in the
5 (as
8-2
all the the
blade
efficiency.
The
others,
and from
is shown
about
double
2 and data
that
loss
importance evident the
from here
in
losses
that
for
tip
for
the curves
as figure
8-2 shows small
from
losses
for the impulse
efficiency
4) as obtained
of figure
of tip-leakage
a single-stage
height,
of the
and reproduced
single-stage
The
loss is clearly to blade
estimates
fig. 1.6)
experimental
estimates
are
from
unshrouded.
clearance
were
(refs.
results
turbines were
of tip clearance
turbines
turbines
in reference
test
3) reaction
plays ratio
in figure
single-stage
published
represent
All turbines
for the reaction dashed
8-2
(ref.
(ref.
For
efficiency turbine. the two
clearance
underturning
for this
two-stage
the level figure.
gives
lines
turbine
The
I,
8-2. solid
impulse that
tip This
and
in efficiency
I
of tip
clearance
increasing
aerodynamically decrease
8-2.--Effect
smallest
with
I
.02 .04 .06 .08 .10 Tipclearance,fractionofpassageheight
figure
8-3. 8-3
clearances. 227
TURBINE
DESIGN
AND
APPLICATION
1.00
•99
.98 U O
.97
r-
8
•95
.95--
.1 .2 .3
¢-
.o
•94
.4
_J r'-
•93
•92 -b-
.91--
I
.90 0
FIGURE 8-3.--Tip-clearance
Reviewing loss
the results
in efficiency
large
ratios
creasing
the
schemes
can
be used
impulse
turbine
the
tip
blade
A clearer
both
8-4
loss mechanisms
flow,
of the are
blade-height consist (3)
and three
blade These
with
The blade
leakage
at
to
flow
with
in-
The
single-
ratios
recessed
are shown
of tip
casing
and tested
in figure
8-5.
is possible
affecting
as compared loading
tip-
configurations
characteristics factors
the
tip while loss-reduction
several
the
general results
configuration of the
tested
performance
considered.
for reducing the
or in combination.
the
that the
and for moderate
a tip shroud.
without
of (1) reduced
mixing
above
4 was
shows
it is apparent
methods
casing
individually
of reference
from ref. 5.)
the loss is appreciable•
clearance,
adding
blades• (Data
and 8-3,
height,
the
.03
reaction,
4, and the turbine-performance
configuration
228
and
either
height,
Figure
tip
recessing
understanding
for the reduced leakage
the
8-2
increasing
to blade
height,
to blade
in reference the
include
shroud•
I
for unshrouded
in figures with
to reducing
losses
clearance
shown
increases
leakage
stage
correlation
of tip clearance
In addition
I
.01 .OZ Tipclearance,fractionofpassageheight
turbine
work
to a zero-clearance
area,
if
(2)
clearance-gap
channel
throughflow,
MISCELLANEOUS
LOSSES
R_s_casi_
Flow -_.
E
"- Rotor blade
(b)
(a)
Tip shroud-_
_',-Rotor blade
Flow_
(c) (a) Reduced blade zero-clearance
height (relative to blade height). (c) Shrouded rotor. 8-4.--Tip-clearance configurations investigated
FmvaE
and
(4) blade
to the
suction
extended clearance fore, was
the
side).
to the
to the blade,
With
the blade Note
the
outer
changed blade
because
reduced.
(as a result
passage
gap was reduced
reduced
further
unloading
of the from
area
indirect
unloading
casing.
for impulse
turbine
of flow going
recessed-casing radius
by varying
loading
(b) Recessed
was
the
amount
of constant
was eliminated, path.
was eliminated, figure
8-5,
the
however,
and With
the height
of casing the the
blade There-
leakage shroud
side as the
recess.
and the leakage that
4).
pressure
configuration,
and
leakage
from
(ref.
flow added
flow was
at tip-clearance 229
TURBINE
DESIGN
AND
APPLICATION
"O
R
38
I
1
.04 .06 .08 .10 Rotortipclearance,fractionofpassageheight
i
.12
36
FIGURE 8-5.--Effect
fractions longer
of tip-clearance
below
some
provides
an
The to other the
turbines.
leakage
difference
but
extend In
the
by The
diameter
(larger
loss increases
clearance as the
and
diameter) gap
to an
different
With
gap
blade-tip not
apply
blade,
since
and
pressure
respect
the blade
to
should
section
will
the not
just
be
losses.
a complicated
easily
no
clearance
span
that
flow
predicted
for a turbine
of clearance
attributed
shrouded
used.
from
shroud
and may
overlapping
is not
for larger ratio
of the
be noted
presents
required
for
clearance
additional
loss
be
the
as the
design
the
the
creating
gap
8-5
of seals
If it does,
factors
clearance
on
can
casing
true
only
efficiency. (Data
instance,
This
particular
it should
fluid and
many
in this
in figure
that
number
tip-clearance
accuracy.
230
the
recess.
stagnant
summary,
influenced
the
not
on turbine
and
is particularly
configuration,
into
churning
on
shroud
shown
depends
also
recessed-casing
0.035
in efficiency.
upon
This
flow
about
results
dependent
I
configurations ref. 4.)
loss between
comparative are
value, increase
increasing friction is decreased. geometries
I
with
depends and,
to blade
problem consistent
primarily
as seen height
previously, increases.
on
MISCELLANEOUS
For
any
given
increasing maintain
for
to
and
hence
therefore, larger
the
case,
leakage
small the
ratio
blade
tip-clearance
It
becomes
of clearance
height,
If tip
it might
the
ratio.
loss is more
turbines.
particular
therefore,
tip-radius
a desired
turbine, ratio,
diameter,
hub-
severe
leakage
for small
disk-friction
height
as the
a given
radius
and
to carry
out tests
be worthwhile
some
a small rotor
disk.
near
the
engine
tive
nature
throughflow
turbines
steady
the
timating
loss
less severe
a problem
in a
to evaluate
the
the
cooling flow
of cooling the associated
gas
outward patterns gas
with
shown
skin
the
base
aircraft
disks
in figure
The
without
8-6.
cools from
qualitaand
Equations
In
engines, and
surface
of the blades.
and
casing.
bathes
rotor-disk
rotor
friction
stationary
gas that
along
to the
to the
and the
for example
are presented
with for
es-
layer
of
herein.
Throughflow
no throughflow,
fluid close to the rotating
flows
around
are
losses No
the case
is due
disk
of lower-temperature
centerline
of the
loss)
rotating
for hot applications,
stream
This
LOSS
(or windage
of fluid between
addition,
For
turbines
to
effects.
circulation have
For
to be
with
diffacult
to blade
smaller.
is considered
DISK-FRICTION The
loss increases
increasingly
gap
becomes
LOSSES
surface
as in figure is thrown
8-6(a),
outward
by
the
thin
centrifugal
action
7//A//////////_
(b)
(a_
(a)
Without FmuaE
throughflow. 8-6.--
(t)) Flow
patterns
for
With rotating
throughflow. disks.
231
TURBINE
and
DESIGN
returns
AND
via
the
up a continuous side of the disk
APPLICATION
stationary
wall
circulatory
to the
effect.
inner
Consider
radius,
an
thereby
element
building
of area
on one
dA = 2,rr dr where
A is the area,
in m or ft,
of the
(8-1)
in m 2 or ft 2, of one side area
element
lb/ft _, acting over this the disk rotation of
area
dA.
at the
The
of the fluid
radius
disk,
shear
and
r is the radius,
stress
r produces
r, in N/m
a resisting
2 or
torque
to
dMo - r2rr 2 dr
2 where
Mo is the
in the
case
resisting
torque,
of no throughflow.
in N-m The
(8--2)
or lb-ft,
shear
for both
stress
can
sides
of a disk
be expressed
as
C/
(8-3) where C!
fluid shear-stress
9
conversion
P
density,
v.
tangential
At the
disk surface,
coefficient
constant, kg/ma;
1;32.17
lb/ft
(Ibm)
(ft)/(lbf)
(sec 2)
_
component
of fluid absolute
the fluid tangential
velocity,
velocity
m/sec,
ft/sec
is
V_ = too where into
w is the angular (8-3),
the
total
velocity, torque
(8-4)
in rad/sec. for both
By substituting
sides
of the
disk
equation
(8-4)
can be written
Mo = fo a 2__#Cip_2r 4 dr where
a is the
disk rim radius,
(8-5)
in m or ft. Performing
the
integration
yields
w2a 5 --
Mo=CM,op
as
(8-'6)
2g where friction
CM,o is a torque loss
expressed
coefficient
for the
as power
ease of no throughflow.
is then
the
torque
times
The the
disk-
angular
velocity: Mow Pd$ --
pwaa 5 -- CM,o
J where 232
Pd/is
the
disk-friction
power
---
(8-7)
2gJ loss,
in W or Btu/sec,
and
J
is a
MISCELLANEOUS
conversion
constant
equation
(8-7)
(equal
that
to
is found
1,
or
in most
778
(ft)(Ib)/Btu).
handbooks
is
Pdl = KdlpNaDr
LOSSES
The
form
5
of
(8--8)
where Kd!
disk-friction
N
rotative speed disk rim diameter
Dr
A number equation made
(8-8)
assortment
doubt,
due
model the
is that
a smaller
diameter
four
picture
modes
casing the
effect
flow
speed,
has been
several
rotating
and
the
and
Flow,
casing across
are the
in the
in the gap.
The
empirically,
is
theoretically
and
radial
and
that
space
on the
chamber
coefficient in each for the
so that
torque
a
tangential
general,
between
the and
evaluated of
coefficient
are as
layers
on the
variation
indicates
components
equation
In
a
A description
continuous
8-7(a)
7) to deterto present
dimensions
Boundary
s. Figure
best
the (8-7)
by having
CM.o was
regime.
Clearance.
and
6 and
can exist in the axial
gap
of the variations
(refs. friction
exist.
merged,
axial
the
between
equation
may
equations
at a given
radius
of flow
torque
Small
from
and
loss is obtained
on disk
experimentally
associated
I: Laminar exists
The
somewhat
speed.
depending
number. and
lower
The
this loss is, no the
in the space
be noted
have
data.
is derived,
conducted
modes
disk,
can occur
rotative
proportions
Reynolds
disk
velocity
blade
a higher
(8-7)
can
of chamber of the
the
each regime follows:
rotor
that
investigation
theoretically
Regime
thing
to predict
Kds in
others
available
geometry,
equation
of flow, or flow regimes,
and
both
and
used
constant
while
fit the
test-apparatus
of flow that
One
of the
circumstances, to better
which
for a given
An extensive clearer
types
casing.
values
equations
of the from
of different
the
exponents
of semiempirical
or (8-8)
mine
published
for different
to the
to variations
oversimplified and
have
to be used
changes
wide
rotor
coefficient
of investigators
small
existence
power-loss
for torque
the
in
nature
of fluid
velocity
coefficient,
both
211-
CM.owhere the
s is the Reynolds
axial
distance,
number
(s/a)i
_
in m or ft, between
defined
(8-9) disk
and
casing,
and
R is
as wa 2p
R = --
where
u is the
dynamic
viscosity,
in (N)
(8-10)
(sec)/m
2 or lb/(ft)
(see). 233
TURBINE
DESIGN
AND
APPLICATION
Radial component ofvelocity
Tangential component of velocity
0 Disk r_
"_}/////////////////////A_ (a)
Radial component ofvelocity
Tangential component ofvelocity
0
0
r(d I
(b)
(a) Flow regimes I and Ill. (t)) Flow regimes II and IV. patterns around rotating (links without
FIGURE 8-7.--Velocity
Regime
II:
Laminar
ness of the boundary
Flow, layers
axial gap, and between ing fluid in which no the
variations
case. arc
The
best
in the
Large on the
Ch,arance. rotor
and
The
theoretical
and and
tangential
velocity
empirical
combined
on the casing
these boundary layers there change ill veh)city occurs. radial
throughflow.
equations
exists Figure
thick-
is less than
the
a core of rotat8-7(i)) shows
components for torque
for
this
coefficient
CII
CM.o--
(8-11) 1_
where 234
CII is a function
of (s/a),
112
as shown
in figure
8-8(a),
and
MISCELLANEOUS
LOSSES
3.3_
3.1
m
2.9 2.7
I
2.5
I
I
I
I
I
I
1
I
I
.10 .15 .20 .25 Ratioofaxialgaptorim radius, s/a
.30
.09
.oz
I
0
.05
(a) Flow regime II. (b) Flow regime IV. FIGURE 8-8.--Evaluation of torque coefficients. (Data from ref. 6.)
CM.o --
3.70 (s/a)
1/1o
(8--12)
R 1/2
respectively. Regime counterpart for torque
III:
Turbulent
of Regime coefficient
Flow, I. The
best
Small
Clearance.
theoretical
and
The empirical
turbulent equations
are 0.0622 CM,o--
(s/a)
V4RV4
(8-13)
and 0.080 CM,o-- (s/a)1/6R1/4
(8-14)
respectively. 235
TURBINE
DESIGN
Regime
IV:
counterpart tions
AND
APPLICATION
Turbulent
Flow,
of Regime
for torque
II.
coefficient
Large
The
best
Clearance.
theoretical
The and
turbulent
empirical
equa-
are Civ
C_,O-RI/5 where
Civ is a function
of (s/a),
(8-15)
as shown
in figure
O.102(s/a) C_,o -
8-8(b),
and
1/l° (8-16)
RII5
respectively. The
particular
determined
by plotting
equations several of figure the
flow regime
(8-9), values 8-9
torque
(8-11), of s/a.
at any
coefficient and from
determined
against (changes
by matching
_'lOI---
_ IV
lines
with
flow; separate
Ratioofaxialgap to disk rim radius,
- --00, %_
- _
:_I I I I I 1o2 lo3 I@ lo 5 lo 6 ld Reynolds number,
236
lines
boundarylayers
_\
,L
FmuRE 8-9.--Theoretical
Turbulent
_
'_ \\
"_
for
boundarylayers _
\ \
_,\_,, I "\\
of the
Laminarflow; merged boundarylayers Laminarflow; separate boundarylayers Turbulentflow;merged
III \
slopes
in the
I
_'_ \
the
from 8-9
In this figure,
Description
II
•,
in slope)
to another.
can be
number in figure
Flow regime
'
-2
number
Reynolds as shown
one regime
Slopeofcurve
_10
Reynolds
(8-15),
discontinuities
transition
are
exists
(8-13),
The
indicate
flow regimes
that
,05
I [ ["1 I@ I@ lol° lon R
variation of torque coefficient with Reynolds number for no throughflow. (Data from ref. 6.)
MISCELLANEOUS
those
shown
determined water
in the
insert
in the
experimentally
and
figure.
with
oil for several
values
Torque-coefficient
a 50.8-centimeter of s/a verify
values
(20-in.)
the
LOSSES
(ref.
6)
disk rotated
in
theory.
Throughflow For the the
case of the
friction
torque
rotating
disk
increases
with
with
velocity
The
symbol
core
of gas
AM,
over
and
leaves
Ko represents to the that
momentum
the
without
of the
at the
angular
ratio
where
Q is the
with
some
of the angular of the
throughflow
disk.
is the
through
AM=2p
volumetric
throughflow of the
M = Mo+AM
value
An
assessment
friction
torque
throughflow
of the of the
velocity
velocity
of the
The
K_a. rotating
in torque, of angular
rate,
disk.
The
2
loss
or fP/sec,
torque
p QKowa
for the
in the through-
(8-18)
2
g
can
throughflow
(8-17)
in m$/sec total
0.45 for s/a ratios
power
increase
of change
Q K_a g
- CM'°pw2aS+2
of Ko is approximately
has been
angular
rate
2g The
problem
the system:
Q- (gowa)a=2p g
clearance space on one side flow case is then
This
8--6(b),
with regime-IV flow. In this case, chamber near the centerline with no
rim
velocity
fluid flowing
as in figure
the throughflow.
analyzed for low values of throughflow it is assumed that the fluid enters the angular
throughflow,
from
be obtained
case
0.025
by
compared
to
to 0.12.
calculating that
of
the
the
no-
case: M --=It Mo
2pQK_a
_
4Ko
-1+
CM
1
Q ,o wa
(8-19) 3
-_ C M,op_a 5 Substituting
equation
(8-16)
M
for CM,o yields
KoR 1/5
--_-o= 1 + o.0255is/a)l/l where
T is a dimensionless
Q ° we _
throughflow
V= _
= 1 +39.2
number
Ko (s/a)m defined
o
T
(8-20)
as
Rm
(8-21)
wa
According that
are
to the
somewhat
data high;
of reference moreover,
7, equation the
effect
(8-20) of s/a
predicts is not
values
accurately 237
TURBINE
DESIGN
AND
APPLICATION
Ratio of axial gap to disk rim radius, sla
f
/o.o,
_
1.
--
1.
--
.12
1.2--
g
10 0
.01
.02
.03
Throughflow
FIGURE
8-10.--Empirical
variation
of torque ref.
given
by
(s/a)
+ 5 percent
m°.
.04
Empirically,
.05
number. T
the
with
throughflow
number.
(Data
test
data
are
represented
to within
by the relation M
T - 1 + 13.9Ko
(8-22)
Mo Equation
(8-22)
is plotted
(s/a) in figure
8-10
Full-admission turbine
axial-flow
unusual may
be a better
so small
that
a normal
heights,
then
it may
due
to partial
with
freedom
In addition, of larger
use of partial 238
for a given diameter
design
admission
may
would
blades
may
rotative higher
speed,
be a convenient
way
mass-flow very-small
admission.
be less
The
than
the
turbine
partial
blade-jet
applications;
a partial-admission
give
of the full-admission
and
values.
most
the design
to use partial
long
losses
for
for which
If, for example,
full-admission
admission
used
arise
be advantageous
and low Reynolds-number blades.
are
sometimes
choice.
s/a
LOSSES
turbines
conditions
1/8
for several
PARTIAL-ADMISSION
however,
from
7.)
ratios.
to reduce
is
blade losses leakage
having
admission speed
rate
short
allows
the
Also,
the
power
output
MISCELLANEOUS
of an existing passages). output
turbine (physically
full-admission
In general,
partial-admission
and low volumetric-flow
As mentioned are the emptying loss.
The mechanisms but
referred
they do result
turbine
The pumping
loss is that
loss caused
several showed power
that
the
effects
loss are quite terms.
rows,
open
casing
sides
empirical
blade
loss
perhaps
in to,
for the
are
disk-friction
in the
accounted
Therefore,
for
pumping-
in the exponents
of obstructions
of such
were
of
investigations
on the
by variations
These
results
equations
these
diameter
and location
the
The
from
and
loss.
8, where
summarized.
resulted
height
most
and efficiency
full admission. in form
(adjacent
vicinity
of the
three
for only by differences
it
for pumping-power
one equation
power
or fully
rotating
or lack
coefficient.
expression
clearly
similar
as evidenced
etc.)
with
sector. or sector
blades
that
channel
are not
to reference
the nature
wall,
of the
applicable The
uncertain,
Further,
active
by the inactive
back
of blade
the
losses
filling-and-
scavenging,
in output
expression
loss
the
for it are somewhat
investigations
pumping-power
on these blade
the
to trace
experimental
estimating
the
with,
all seem
and
through
operating
and expressions
combined
expressions
partial-admission
losses
in a decrease
to the same
and often
pass
of partial-admission
casing,
of the stator
high specific-work
channels
to as expansion,
compared
a fluid-filled
have
the
blade
as the blades
loss has been
understood,
chapter,
inactive
loss encountered
latter
when
in this
loss in the
This
turbines
some
rates.
previously
pumping
block
LOSSES
appears
that
in
a generally
loss is yet to be found.
often
used
is
(8-23)
Pp = KpoU,,,al l'sD,,, ( 1 - _) where Pp
pumping-power
loss, W;
K_
pumping-power
loss coefficient,
u.
blade
mean-section
l
blade
height,
D,,
blade active
mean-section diameter, fraction of stator-exit
E
The
value
to the for
units
an
values the
used
friction
coefficient herein
by
turbine
loss estimated
losses
of reference
equation
(8-23),
(sec _)/(Ibm)
(lbf)
(seO)/(Ibm)
(ft 3n)
ft/sec
For and
same
coefficient
(ft3n).
This
rotors
of the
pumping were
by equation if the
in reference
l/m _/2, or 0.0105 the
housing
9 and the
m; ft area
to one-half
disk-friction the
1/m_/_;
m/sec;
Kp as reported
is 3.63
rotor.
one-quarter
combined
speed,
(lb)/sec
m; ft
unenclosed were
enclosed
(lbf)
of the
(ft)
(8-7)
(lbf)
losses
from
to be 5.92 higher
recently,
a single-stage
loss is converted
Kp is found is significantly
(fts/2), coefficient
More
in reference
is subtracted
remaining
the
values. for
converted
(sec2)/(lbm)
enclosed,
above
reported
8 and
than
rotor
9. If a diskthe
combined
to the
form
of
]/m _/_, or 0.0171 the
coefficients 239
TURBINE
DESIGN
reported lack
other
Imagine filled
8, and
momentum
fluid
less
passes
to the
leaving
out
of the
fluid passing
of the
fluid.
where
by
sector,
into,
cause
The
effect
multiplying
pitch,
sector
loss
on
the associated velocity diagram work of an axial-flow turbine as
and
has
the
decrease
(2-14),
geometry,
we
can
energy
in momenby
nozzle
a loss
active
arc
that
ac-
coefficient
efficiency
and
as it flows
in the momentum
f is the
Wu ,2) = _Um ( Wl sin 01-
( W_ a-
less
velocity
turbine
(2-6)
arc,
momentum
in m or ft, and
As the
the available
this
blade
fluid
diffused
decreasing
until
the
this
decrease
K, is a rotor
As
active
Since
rotor-exit
It is high-
loss occurs.
nozzle
10 that
the
the use of equations
Ah' = g_
thus
loss.
sector.
sector.
it is rapidly
in reference
rotor-blade
of the
With
the
sector
out by the
sector
an overall
the rotor,
in m or ft. Effectively, for the sector loss.
follows.
the
will continue
active
channel.
the
active
scavenging the
off from
to flow losses
the
be pushed
a second
the
reported
be found
This
enters
through
It was
p is the
length, counts
area
These
must
within
is cut
fluid
channel
of the
to primarily
be called
to enter
that
nozzle.
active
channel
the rotor.
tum may coefficient
the
herein
starts
fluid
is completely
blade
blade
through
as it just
stagnant
high-momentum
entire
is attributed
loss shall
channel
channel
channel
difference
loss model.
relatively
blade
the
partial-admission
a blade
with
inlet
APPLICATION
in reference
of an adequate
The
the
AND
is determined from
volume
express
the
as 1, and
specific
(s-25)
W2 sin 02)
where Ah'
turbine
Wu W
tangential
0
fluid relative
The
relative
subscripts
an impulse
specific
work,
J/kg;
component velocity,
1 and turbine
of relative
m/sec;
angle
velocity,
m/sec;
ft/sec
ft/sec
measured
2 refer (which
Btu/lb
to the most
from rotor
axial inlet
direction, and
partial-admission
exit,
deg respectively.
turbines
are),
For where
01= -02, Um Ah' = _-_ W, sin Ox(1 +K,_) where turbine. 240
K_ is the For
rotor the
relative-velocity
partial-admission
ratio turbine,
W2/W_
(8-26) for the
applying
full-admission the
sector
loss
,
MISCELLANEOUS
coefficient
LOSSES
yields W_ = KwK,WI
So, for the partial-admission
(8-27)
turbine,
Ah'r_=-_
(8-28)
Wt sin _I(1+K_K,) qJ
Since
efficiency
is hh' (8-29)
- Ah_a where
Abed is the
turbine
ideal
specific
work,
in J/kg
turbine
with
respect
ficiency of the partial-admission admission turbine is
nm
or Btu/lb, to that
the
of the
Ahrro
effull-
(8-30)
Ah' Substituting
equations
(8-26)
and
(8-28)
into
equation
(8--30)
then
yields I+K,,K, 1 -I-K_
_=n The
efficiency
sector
penalty
loss only;
efficiency turbine
the
further. rotor
should
as more
increase.
Also,
is not
admission
study
was
determined
total
loss due
between and
the
closely of the be done
a range
losses
were
to leakage
admission in figure with stant
losses 8--11.
decreasing over
Predicted
from
the
of reference The arc
fraction,
the range
of arcs
cfficiencies
from
pumping while
the
sector
loss;
loss will
on the
pumping
of a partial-
was
taken
separately
to the
other
turbine
as the The
and
The
difference
blade were
pumping subtracted
was called other partialsector loss and any loss
inactive
against and
axial-flow
12 to 100 percent.
efficiencies.
loss to give what losses include the sector
blades
of a small
operation
9 are plotted
combined
profile
at present.
efficiency
measured
active
the
blade
optimization
of admissions
to partial-admission
the overall
a partial-admission
the
of rotor
analytically
for the
to reduce
rotor,
complete
accounts
will reduce
that
blades
the full- and the partial-admission
disk-friction
earlier
to the
9, the
from the total partial-admission admission losses. These other due
spaced
the
of reference
(8--31)
indicates
number
Therefore,
over
equation
loss discussed
are added
effect cannot
by
(8-24)
have
blades
known. design
In the
pumping Equation
however, loss
expressed
(8-31)
sector.
partial-
admission-arc
disk-friction losses
The
fraction
loss
remained
increased
nearly
con-
tested.
(from
ref.
10) are plotted
against
blade-jet
speed 241
TURBINE
DESIGN
.6
AND
APPLICATION
T
-- - -- Estimated pumpinganddisk-frictionlosses
i.5
C3 0
I I I
K.4
Pumping anddisk-frictionlosses Otherpartial-admission losses
I
I "I"
'Is
I I t
C
% .|
-
gJ .1
0
Fmtmm
.2
8-11.--Variation
l
I
I
I
.3 .4 .5 .6 .7 .8 Activefraction of statorexitarea, •
.9
1.0
of partial-+_cimission losses with active area. (l)ata from ref+ 9.)
fraction of stator
mission
o ,a U
qJ
$
.1
I .1
.2
.3 .4 .5 .6 Blade-jetspeedratio, Urn/_
Fmuam 8-12.--Design-point
ratio
(see discussion
operating admission. admission reduction Aerodynamic 242
with The
performance of partial(Data from ref. 10.)
in vol.
1, ch. 2) in figure
full admission expected
is seen.
The
in optimum efficiency
and
reduction important blade-jet
with
three
in peak thing speed
is a maximum
.7 .8 Ahtd
8-12
turbines.
for a particular
different
to note
1.0
and full-admission
efficiency
ratio
.9
amounts with
from
at a blade-jet
of partial
reduced
this
as admission
turbine
arc
speed
figure
arc
of
is the
is reduced. ratio
of 0.5,
MISCELLANEOUS
irrespective
of admission
Blade-pumping blade
and
speed, arc
maximum
net
and
design
decreases.
speed
into ratio
which
The
decrease
as
admission
arc
power
minus
at lower
turbine, before
blade with
(aerodynamic
speed.
decreasing
aerodynamic
blade
power
is reduced,
as the
blade-pumping
speeds.
Thus,
the partial-admission
an optimum
for the
losses
or near-optimum
must
be
blade-jet
can be selected.
INCIDENCE
row
decreasing
gross
is obtained
design
with
of the
Therefore,
power) the
part
power
of a partial-admission
factored
decreases losses,
a larger
output
disk-friction
and
disk-friction
become
admission
arc,
LOSSES
incidence (either
loss is that
stator
angle.
Flow
since,
theoretically
design
condition.
shown
in figure
is the camber is defined as
loss which
or rotor)
at some
would
normally
incidence
at least, The
occurs angle
The
and
all gas
and line
the
i
blade
used
dashed
defines
a
--
the gas enters than
the
angles
when
are
speaking through
inlet
angle.
The
a blade
optimum
at off-design
running
blade
=
when other
only occur
nomenclature
8-13. line
LOSS
flow
conditions,
matched
at the
of incidence the
is
blade
profile
incidence
angle (8-32)
ab
where i
incidence
angle,
fluid flow angle ab
blade
The
inlet
for
indicated because angle
rotors.
from
angle
fluid flow angle
angle
deg from
must
The
axial
direction,
axial
be the
incidence
deg
direction,
absolute angle
deg angle
may
for stators be
positive
in figure 8-13. The sign of the incidence cascade tests have shown that the variation
is different
Axial direction
for positive
and
negative
and
the relative
or negative,
as
angle is important of loss with incidence
angles.
Vp /
IB,
i -a - ob
FIOuRE
8-13.--Blade
incidence
nomenclature.
243
TURBINE
DESIGN
AND
APPLICATION
Low-reaction _/_ blades-_. o.
n •*,._/2___
_,_i_
U.j'_''_
Incidence angle,
The
8-14.--Characteristics
FiauaE
8-15.--L(ical
general
is shown
The
incidence.
figure
at large
may
positive
whereas
low-reaction
range. Another not
nation
thing occur
incidence.
This streamlines
cidence
is larger
be due
blade
and
the inlet
have
of incidence
to some
have
to be noted at zero may
from
incidence,
be explained for
other angle.
two
figure
small
tests
the
and
angle test
zero incidence
incidence
in figure
higher
flow
incidence of cascade
than
angle,
for
negative
on the suction
surface
8-15,
and
the
lack,
value of negative incidence. of the gas flow is large over
losses 8-14
at some
by the
inlet
at some Both
about
of incidence
but
surface.
loss with
local separation
range
loss.
a summary
positive
as indicated
blades
incidence
on blade
represents for
a wide
streamline curves upward and the true zero incidence 244
which
incidence,
blades)
the
separation
area, of separation at the same in which the mean acceleration
reaction
does
flow
is not symmetrical
a loss that This
i
of blade
of the variation 8-14,
loss curve
shows
smaller blades
nature
by
results. but
FIGUaE
b de
for
negative theory
as the flow impacts occurs when there
the
is that small
sketch
angles
which
the
8-16. one
incidence
with
that
loss
of negative
shown;
show
incidence
minimum
of figure are
loss is low,
same
amount
or
Also, (high-
the
The at
stag-
zero
in-
respect
to
stagnation
on the blade leading edge, is some negative incidence
MISCELLANEOUS
LOSSES
a
ab
F[aua_
8-16.--Curvature
relative
to the
free-stream
usually
-4 ° to -8 °. Because
blades because
with a small amount of the small difference
The
magnitude
off-design An
component any
that entry
recovered
incidence
here
to the
into
blade
parallel
loss and energy
the
kinetic-energy
and
to account
negative
loss due
on
be
others
importance
their do not
when
the
predicted.
A method
for
data
is described
in reference
11.
with
the
aid
a component direction passes
normal
of figure V.
8-13.
normal
The
to, and
a
(camber
line at inlet).
through
the
component
(V,_ \-_J
2
V_' =2_
blade
is entirely
c°s_ i
to incidence
is
V12 -2_ (1--cos
2i)
for the
incidence,
loss not occurring to
while
loss is
design
row lost.,
is
Li-
In order
incidence, takes
inlet the
at minimum
designers
component
that
angle
turbine
must
on test
V_ 2 VI' 2gJ-2gd and
some
loss
is described
the
kinetic
incidence
of a turbine
Vp parallel
stre,_mline at blade inlet.
of negative involved.
V_ can be resolved
If it is assumed the
The
of this,
loss based
method
velocity
without
of the
incidence
analytical
inlet
flow.
performance
determining
of stagnation
differences
the effect
(8-34)
in loss variation
of blade-row
at zero incidence,
(8-33)
reaction,
equation
(8-34)
and
with
positive
the minimum
has been
generalized
V12
L,=_
I-l--cos"
(8-35)
(i-io7,_)"1
zg,I where equation
ion, is the has
optimum
proved
(minimum-loss)
satisfactory
when
incidence used
angle.
in off-design
This
type
of
performance 245
TURBINE
prediction loss
data
positive
DESIGN
AND APPLICATION
methods are
such
lacking,
incidence
have
as that
values been
of reference
of n = 2 for used
12. Where negative
specific
incidence
incidenceand
n = 3 for
satisfactorily.
REFERENCES 1. HORLOCK, JOHN H.: Axial Flow Turbines. Butterworth Inc., 1966. 2. HOLESKI, DONALD E.; AND FUTRAL, SAMUEL M., JR.:Effect of Rotor Tip Clearance on the Performance of a 5-Inch Single-StageAxial-Flow Turbine. NASA TM X-1757, 1969. 3. KOFSKEY, MILTON G.; AND NUSnAUM, WXLLIAM J.:Performance Evaluation of a Two-Stage Axial-Flow Turbine for Two Values of Tip Clearance. NASA TN I)-4388, 1968. 4. KOFSKEY, MILTON G.: Experimental Investigationof Three Tip-Clearance ConfigurationsOver a Range of Tip Clearance Using a Single-StageTurbine of High Hub- to Tip-Radius Ratio. NASA TM X-472, 1961. 5. HONO, YONO S.; AND GROH, F. G.: Axial Turbine Loss Analysis and Efficiency Prediction Method. Rep. D4-3220, Boeing Co., Mar. 11, 1966. 6. DAILY, J. W.; AND NECE, R. E.: Chamber l)imension Effects on Induced Flow and Frictional Resistance of Enclosed Rotating Disks. J. Basic Eng., voi. 82, no. 1, Mar. 1960, pp. 217-232. 7. DAXLY, J. W.; ERNST, W. I).; AND ASnEDIAN, V. V.: Enclosed Rotating Disks with Superposed Throughflow: Mean Study and Periodic Unsteady Characteristics of the Induced Flow. Rep. R-_4-16, Massachusetts Inst. Tech. (ARO1)-2500-2, AD-443060), Apr. 1964. 8. STODOLA, A. (Louis C. LOEWENSTEIN, TRANS.): Steam and Gas Turbines. Vol. I. McGraw-Hill Book Co., Inc., 1927. Reprinted by Peter Smith, 1945, pp. 200201. 9. KLASSEN, HUOH A.: Cold-Air Investigation of Effects of Partial Admission on Performance of 3.75-Inch Mean-l)iameter Single-Stage Axial-Flow Turbine. NASA TN D-4700, 1968. 10. STENNING, ALAN H.: Design of Turbines for High-Energy-Euel Low-PowerOutput Applications. Rep. 79, Dynamic Analysis and Control Lab., Massachusetts Inst. Tech., Sept. 30, 1953. ll. AINLEY, D. G.; ^ND M^THIESON, G. C. R.: An Examination of the Flow and Pressure Losses in Blade Rows of Axial-Flow Turbines. R&M-2891, Aeronautical Research Council, Gt. Britain, 1955. 12. FLAGO, E. E.: Analytical Procedure and Computer Program for Determining the Off-De._ign Performance of Axial-Flow Turbines. NASA CR-710, 1967.
246
MISCELLANEOUS
LOSSES
SYMBOLS A
area
¢t
disk rim radius,
CII Civ
coefficient
C/ CM
,o
on one side
of rotor
disk,
m2; ft 2
m; ft
used
to evaluate
Ci.o
in regime
I I by equation
(8-11)
coefficient used fluid shear-stress
to evaluate coefficient
Ci,o
in regime
IV by equation
(8-15)
torque
coefficient
with
no throughflow
D
diameter,
f
nozzle
9 Ah'
conversion turbine
specific
_h_d
turbine
ideal
i
incidence
J
conversion
Kdl
disk-friction
Ko
ratio
Kp K.
pumping power loss coefficient, sector loss coefficient
K,o
rotor
Li l
incidence
M
frictional lb-ft
N
rotative
n
exponcnt
m; ft active
arc length, constant, work,
rotor-blade volumetric
1/mY2;
angular
velocity
(lbf)(seC)/(lbm)(ft
for full-admission
torque
tad/see;
impulse
'v2)
turbine
Reynolds radius,
8
axial
distance
U
blade
speed,
sides
of rotor
disk,
N-m;
h)ss, W ; Btu/sec Btu/sec
m; ft
throughflow
r
both
rev/min
loss, W;
pitch,
for
(8-35)
power power
R
rate,
m_/sec;
ft'_/scc
number m; ft
V
absolute
W
relative
between m/see;
velocity,
blade
inlet
rotor
disk and
from
angle
dynamic density,
static
ft/sec
axial
from
axial
direction,
deg
direction,
deg axial
direction,
deg
efficiency
viscosity, kg/m'_;
m; ft
m/sec/ft/sec
fluid relative angle measured from active fraction of stator exit area turbine
casing,
ft/sec m/see;
velocity,
fluid flow angle
P
to disk
m; ft
disk-friction P
velocity
Btu/lb
in equation
Q
pressure
coefficient
coefficient
speed,
pumping
of inlet-total
Btu/lb
angular
resistance
Pp
on ratio
1; 778 (ft) (lb)/Btu
loss, J/kg;
height,
based
J/kg;
power-loss
of rotating-core
blade
(seC)
deg
constant,
velocity
(ft)/(lbf)
Btu/Ib
work
pressure,
angle,
(Ibm)
J/kg;
specific
to exit-static
m; ft
1;32.17
(N)
(sec)/m2;
lb/(ft)
(see)
lb/ft 3
247
TURBINE
DESIGN
AND
T
fluid shear
T
throughflow angular
APPLICATION
stress,
N/m_;
number
velocity,
lb/ft _
defined
by equation
rad/sec
Subscripts: m
mean
n
component
o
no throughflow
opt
optimum
p
component
pa r
partial admission disk rim
u
tangential
1 2
248
section normal
parallel
component
_rotor inlet ],blade-row inlet rotor exit
to blade
inlet
direction
to blade
inlet
direction
(8-21)
CHAPTER 9
Supersonic Turbines ByLouisJ. Goldman A supersonic supersonic have
turbine
relative
potential
having
weights
used
They
have
been
have
been
studied
and/or
used
for space. Supersonic
turbines
puts
because
of the
type
of turbine
would
require
small
number
of stages.
It
atively
simple.
turbines than high
As
ratios are
a minimum
consumption, could
the
more
than
supersonic To
the
proper rotors
chapter, the
ideal
efficiency
are
losses.
For
systems
available
lower
the
optimum
designed
by
supersonic
turbine
following
headings:
must the design
design
(1) method
and (often
low
relless
blade-jet because
primary
high
a
of
design
minimum
fluid
pressure
ratio
and
may
result
in a
the
highest
possible
supersonic
stators
choice.
used.
and
the
this and
supersonic
1),
with
the
turbines
method
level,
ratios
where
out-
fluid
primarily
efficiency
be
power
(vol.
along from
turbine
of supersonic
methods
3
of stages
work
work
however,
efficiencies,
and
systems
specific
speed
(those
available.
be light-weight
2 and
static
the
being
design
chapters
are
of driving
velocities,
a
expansion systems
a given
blade-jet
to low number
offset
turbine
keep
level,
under
in
For amount
jet
low
ratios
large
therefore,
high at
indicated
correspond
ratio.
would,
fluids high
turbopump
for
a small
with turbines
auxiliary-power
potential
pressure
of
pressure
open-cycle
the
operate
exit-kinetic-energy
criteria
and
high
Because
generally 0.2).
speed
have
high-energy
in rocket
in
operates
Supersonic
consequently,
high
NASA use
that
rotor.
where
and',
where
by
for
as one the
in systems
molecular are
is defined entering
application
low
velocities)
stage
velocity
at Both
of
characteristics.
performance of characteristics,
In are
this
discussed (2) design 249
TURBINE
DESIGN
AND
APPI.,I_ATION
of supersonic
stator
(4) operating
characteristics
blades,
(3) design
METHOD The
method
certain tions
of
type
are
chapter. certain
OF
characteristics
is a
of partial
for
two-dimensional
the
of this
type.
Other
types
Only
this
flows)
method
blades,
of flow flow
can
be
for
equation.
supersonic
type
also
general
differential
of supersonic
non-steady
rotor
and
turbines.
CHARACTERISTICS
(hyperbolic)
of motion
gas
of supersonic
of supersonic
flow
will
(i.e.,
solving The
of a perfect
be discussed
axially
handled
by
a
equain this
symmetric this
and
method
(see
ref.1). The by
method
formal
of characteristics
mathematical
siderations.
The
derivation
processes
involved.
ematical
derivation
equations.
Both
It
based
on only
is useful
motion can
than weak
be considered
uniform
through
the
and
compression
wave
subsequently,
one
the
field
weak
flow)
waves an
are
expansion
the
here.
method
to other
is the
flow
waves, shock zero. shown wave
the
waves.
The
Examples figure
is
produced
"// V//////
_UX/, :/;//_Wa II
9-1.
wave
V
" V__ctV
X .....
7"/////i /
(a)
(a) FIGURE
250
(b)
Expansion. 9-1.--Weak
(b) expansion
and
compression
Compression. waves.
waves, entropy
of weak
in
of
a single
Mach
Mach
dV
similar
equations
through
ye
V
math-
2.
called
Mach wa
physical
The
1 and
satisfies
oblique
is essentially
stresses
(1) con-
Wall
that
These
ways:
dynamical
presented
in references
a Single
parallel wave.
to be very
change shown
flow
standing
pansion be
Along
in two
simple
dynamics
are given
supersonic
(other
vanishingly
developed (2) by
in extending
developments
simplest
be
and
will be the
Flow The
can
methods
ex-
As
will
when
the
SUPBRS_NIC
wall bends away from the flow, and a compression when the wall bends toward the flow. The
bend
(of
angular
as a disturbance
which
is to follow
the
a boundary
condition
with
uniform
solution may The the
wall. flow
The
bend
flow
along
a curved
through
a weak
Consider
the
of initial
of mass
requires
expansion standing
wave Mach
velocity
of it.
can,
The
wave
if the flow
be considered
any
as wave
of this
curved
of straight be
The
Mach
importance
that
therefore,
waves.
surface sections.
approximated
dynamics
as
of the
flow
be discussed.
included
V as shown
also
number
will now
can be considered
is a standing
it is realized
of Mach
is produced
is required
may
up of a finite
surface
a series
the wall
wall
sides
wave
which
one solution
when
to be made
through
in the
on both
can be appreciated
flow
dO) in the wave,
to which fields
be considered
rection
magnitude produces
TURBINES
at an angle
in figure
9-2.
The
_ to the
di-
conservation
that A=
p V,, = (p+dp)
( V. +dV.)
= constant
(9-1)
where w
mass
flow
A
flow
area
p
density,
kg/m3;
V.
velocity
component
Neglecting
rate,
kg/sec;
along
Mach
lb/sec wave,
m_; ft 2
lb/ft a
second-order
normal terms
to Mach (i.e.,
wave,
dp dV.)
m/sec;
ft/sec
gives
V.+V dp=o Conservation
of momentum pV.V
in the
(9-2) tangential
,= (p k- do) ('[7. + dV.)
direction
gives
(V ,+ dV ,)
(9-3)
t
Ma¢,// wave/
Z_Z_ n
p
p +dp + dV
dO
U//////////////////_ •. _ /////,
FIGURE 9-2.--Flow
through
a weak
expansion
wave,
and associated
nomenclature.
251
TURBINE
_, I_E,SIGN
where
Vt
is the
m/sec
or
ft/sec.
AND
APPLICATION
velocity
component
Substituting
tangent
equation
to
(9-1)
the
Mach
into
wave,
equation
in
(9-3)
gives
y,,V,=
pV,,(V,+dVt)
(9-4)
or
dV,=o This
means
stant dV
that
the
flow
crosses
to dV,
and
as the is equal
Conservation
tangential the
component wave.
of velocity
Consequently,
is directed
normal
of momentum gp--b pV,,Z=g(p
(9-2)
in the
remains
the
velocity
to tile Mach
normal
change
wave.
direction
+ dp) --b (p--b dp) (V,,--b dV,)
con-
gives _
(9-6)
where g
conversion
p
absolute
constant,
1 ; 32.17
pressure,
Substituting
N/m2;
equation
(9-I)
dV,_ by
using
(ft)/(lbf)
(sec 2)
lb/ft 2 into
O=g Eliminating
(lbm)
equation
dp.-}-pVn
equation
(9-6)
and
expanding
dVn (9-2)
(9-7) results
in
V.--g Equation
(1-57)
of chapter
where
a is speed
process (9-8)
being into
of sound,
considered
equation
1) states
(_)s
in m/sec here
(9-9)
(9-8)
1 (vol.
a---- _/g
(9-9)
or
ft/sec.
is isentropic,
shows
Since
the
substitution
differential of equation
that V,,:a
Therefore,
the
be equal
to the
component speed
yields
(9-10)
of velocity of sound.
normal
Noting
Vn=V
to the
from
figure
Mach 9-2
wave
must
that
sin tt
(9-11)
gives V, sin _V-V where and 252
M has
is the
Mach
number.
meaning
only
for M>
The 1.
a
angle
1 M ft is called
(9-12) the
Mach
angle
SUPF__SONrC
TURBINE,S
Mach wa ve
V
_" _
/ FIGURE
The dV
can
9-3.--Velocity
be 9-3.
du
713
v+dv
relation
figure
"-- -....
diagram
between
for
change
found
from
the
In the
limit
(dO-*0),
flow
through
in flow
velocity
angle
relations
a weak
expansion
wave.
dO and
velocity
change
shown
geometrically
in
du=dV
(9-13)
dv=Vdo
(9-14)
du dV B= _-_= _
(9-15)
and tan where du
component
of dV
parallel
to initial
velocity
dv
component
of dV
normal
to initial
velocity
Since,
as can
be determined
from
equation
V, m/sec;
ft/sec
V, m/sec;
ft/sec
(9-12),
1 tan/_=_/_-1_ equation
(9-15)
(9-16)
1
becomes dV
do
V -- 4_-1 It
is more
convenient
if dV/V
velocity
ratio
velocity
Vcr is equal
to
(M=I)
and
evaluated
(vol.
1). The
M*=V/VcT can relation
be
rather the
between
is expressed than
speed
Mach
of sound from
M*
(9-17)
and
in terms number at
equation M is given
the
of the M.
The
critical
(1-63) by the
of
critical critical
condition chapter
1
equation 253
TURBINE
l)E_IGN
AND
APPLICATION
/ M=
2
/
7 is the
heat
at
ratio
constant
temperature
of specific
volume.
_
_+i
V where
M,
1
(9-18)
7--1
heat
Since
M,
_
at constant
Vc,
is
pressure
constant
to specific
(because
the
total
is constant), dV V
Substituting
equations
(9-18)
dM* M*
and
(9-19)
(9-19)
into
equation
(9-17)
gives,
finally, dO:
1 M7--1.2-1 M, 7+1
This
is the
velocity relation
could
wave,
bends,
by equation to
type
each
(9-20)
changes
solution
9-4.
been
flow
Assume
that
producing
the
The
surface
through
each
motion
for
Mach will,
flow,
indicated
wave
provided
therefore, values
or simple
wave
.._- _lach waves //
I
\
//
V1
---,.-
/
/
/""
'_
\
, ve
; /
I/ /
",
"-,
>'
, //
d83 FmURE
254
9-4.--Representation
of
flow
along
a
convex
as
of a number
infinitesimal
Prandtl-Meyer
a
surface,
relation
field
and similar
compression
(convex) The
flow
A
sign.
is composed
wave.
combined
of
weak
a minus
a curved
a Mach
will be satisfied
is called
have
angle
wave.
a single
would along
in flow
expansion
for
(9-20)
equations
of flow
a change
weak
obtained
the
in 8 are small. the
between
a single
equation
consider
in figure
of small
This
that
us now
shown
relation
through have
except
Let
the
differential
change
(9-20)
_ dM* M*
wall.
be a of
dO.
flow.
SUPERSONIC
If the
number
continuous.
of segments
approaches
Integration
•0= _1 _I/4/_--4-1 arc_
infinity,
of equation
sin [(3,-- 1 )M*_--
(9-20)
the
TURBINES
flow
field
becomes
gives
_¢]+ 1 arc sin t/'_ _,_-_ -4-1 -- 3,)\ + constan (9-21)
If
the
angle
constant
given
and
it
Meyer
Mach
symbol
such
equation
is tabulated angle
from
is chosen
by
in
is the 1 to
(9-21) many
angle the
that
0=0
when
is called
the
references
through
required
(e.g.,
which Mach
the
M*=I(M=I),
the
Prandtl-Meyer
angle,
ref. flow
number
1).
The
Prandtl-
must
turn
in going
and
is often
the
_ (or u). Therefore,
/,-45
1
given
I_ _r _A- arc sin [(_--1
sin
J"_ --_ 1E2-arc
)M*_--_]
(9-22) Note
that
given
by
the the
change change
in flow in the
direction
respective
Oz-- 01: 50: The waves,
derivation there
the
velocity
sion
wave.
along
has
would
be
decreases This
a concave
means wall,
been
for
a minus (M
(50)
expansion sign
shown
the
from
V1 to V2 is
angles.
That
_2-- _I waves.
for Mach
in figure
is,
(9-23) For
in equation
decreases)
that
in going
Prandtl-Meyer
(9-17).
flow
through
angle 9-5.
compression Therefore, a compres-
_ increases
The
Mach
for lines,
flow there-
hock
Mach waves ,4/,
_\\\\\\\\\\_\\\\\
\"r ....
_o2
d61
FIGURE
9-5.--Representation
of
flow
along
a
concave
wall.
255
TURBINE
fore,
converge
relations, the
DESIGN
entropy
AND
and
of course,
a shock
would
as shown
be invalid
in the
in the
figure.
shock
region
increase.
FIGURE
256
form
APPLICATION
9-6.--Hodograph
characteristic
curves.
The
derived
because
of
SUPERSONIC
The
relation
ratio
M*
(eq.
in figure curves
between
The
9-6.
This
erate
these
An
The
on
the
/)2
must
Mach (shown
in
the
plane.
the
line
wave
The
may
plot.
The
flow
any
two-
has
around
characteristics.
been
M*=
with
critical
hodograph
varied
to gen-
1 at 0----0 represent velocity
ratio
Point
OP2 the
as
After the
P_ is located
parallel
preceding
the
procedure
_
Math
is
wall
by
drawing
diagram
by
Note P1.
the
segment
the the
The This
physical additional
to use.
if it is recalled
that
normal
P_P2.
in
cumbersome
into (line
S_).
through
be
V1
through
direction
continued
at best,
to
segment curve
to
example.
PI is located
hodograph
wall
wave
numerical
field
is divided
point
characteristic
Mach
is,
entirely
in the
V2 is found
process
be made
the
flow
a simple
initial
characteristic to the
the by
the
corresponding
corresponding
to Ur2 (or
V1 and to
9-7(b))
is that
the
allows
explained
wall.
(fig.
figure)
parallel
to
(fig. 9-7(a)),
expansion
separating
This
is best
a curved
characteristics
parallel
plane.
curve
as N1 in the is
as shown
a hodograph
through
are
and
along
to V1).
segments. The graphical cedure
of the
of segments
lie on
velocity
diagram,
hodograph
(9-21)
angle
physical
characteristic
the
called
passing
characteristics
flow
number
direction
are
the
critical
(9-22).
graphically
OP_ parallel drawing
curves
property the
wave
Consider
and
of equation
of Prandtl-Meyer
constructed a finite
of
surface
the
a polar
is called
curves.
to
on
of diagram
constant
important
Mach
be plotted
0 and
characteristic
by equation
normals
angle
are
of the
variation
expressed
can
flow
type
plot
convex
value
the
(9-21))
of this
dimensional
the
TURBINES
The
that
the
lo _-,___.._/
/
prodirec-
waves
-15,-J \
/
\,
Cb_
(a)
Phy,_ical
plane. FIGURE
(b) 9-7.--Flow
along
convex
Hodograph
plane.
wall.
257
TURBINE
I)E_SIGN
AND
/
APPLICATION
'_,]dC h waves
0 cai
(a) FIaURE
(hi
General
9-8.--Flow
case.
along
(b)
convex
wall
with
Math
Limiting waves
case.
intersecting
at
one
point.
tion
of
the
Mach
changes
occur
assumed
that
average
speed
direction
of
may
now
waves
A special shaped in figure
9-8(a).
point
0.
The
seen
that
This
type
corner,
Now
imagine
limiting
of flow
and
case
large
sonic nozzles for this case.
with
The method of solution generalized to handle the uniform figure
parallel 9-9.
amount. As finite and
The
before, number S'_,
represented represents 258
flow
the
that will
$3 and by
the
the
The
a wall
hodograph
point,
approaches
Two
or
to the
Equation
flow both
where
flow design
(9-21)
are
about
constructed initial
P_ in the
by
two
deflected the by
around
a
of super-
is still
valid
hodograph of the
as shown
outward the
here flow
the
of the
dividing
denoted
wall can be the initially
walls
centerline
parallel
magnitude
it is bends.
Walls
bounded
walls
common
of small
flow,
is so
as shown
9-8(b),
a number
corner-type throats.
figure
wall
the
used for the flow along a single flow between two walls. Consider
and
average
past
if the
by
is important
The
usually to the
to the
occurs
wall
later,
Between
be
finite
is
flow
a common
replaced
line segments, S'3.
point
direction
the
called
is symmetric
flow
of straight
and
has
supersonic
Suppose
The
wall
through
that
sharp-edged
Flow
relative
numerically.
is represented
is often
it
corresponding
points.
a single
pass
bend
as will be seen
_. Since
for visualization.
along
lines
angle
two
completely
of flow
angle problems,
measured
the
useful
Math
Mach
two points,
Mach
a single
the
practical
the
between
is still
the
of
at
constructed
case
that
lie
the
flow
though,
by
solution
between the
is given
the
the
be
diagram,
wave
in
diagram. velocity
same
channel.
walls
into
by S_ and field
a
S'_, S_
in region The
in
line
V_. The
1 is OP_ flow
S_PF__
V [
,F 2
.... /!:
>_,""'/L_
.... s3__ i ,////' , si .,,,,_>;_L_
s
S_NIC
TURBINES
\
15v--...
u
I C'I
,
/
c2
]
// 0
P7
_1-5/ J _ "" _///////_ k- V k_V 2
6 _ 3 _///////'_ ,..,,/////.
(a)
(a)
(b)
Physical
plane. FIOUR_
in regions
2 and
be determined, The
lines
The two
2' (points
problem
for the
OP'2
now
Mach
between
what
intersect.
a weak V'2,
fields
diagram)
can
expansion
wave.
respectively.
happens
Flow
plane.
hodograph
through to V2 and
is to determine
Hodograph
walls.
in the
flow
are parallel
waves
two
P2 and P'2
as before,
OP2 and
initial
(b) 9-9.--Flow
to the 2 and
flow
after
the
2' must
be
sep-
---4
arated
by
another
flow
field,
direction. Consider that continuation, in modified A jump
from
region
of motion
only
is,
C'2
C1 or
To
both
satisfy
ing the The the
point
makes
little
physical
makes
sense
direction given in
by
the
flow,
of the the
the
construct across
velocity the
the
P,
flow
channel
are
can
end
point
end
plane.
strikes
are
the
M'2
being
of the P'2P3
of
the
until wall.
equations P2; that
graphically). C'L or C2.
jump
this
further
would
represent-
and
one
P2P3,
A new
type
hodograph The
waves
are
respectively,
symmetry
of the
which
expansion. Mach
procedures
that
waves,
flow initial
plane
mean
P3 in the
assumed
to V_. These
piecemeal
the
(9-21) of the
same
2 and 2' by a M, and M'I.
through
compression
point
segments
Because
V3 is parallel field
and
the
characteristic
because
it represents
to the
satisfy
point
out
sense.
The
in
P3 or P1 in the hodograph
waves
M_
not
from waves
eq.
lie on
the
be ruled
because
can
represent
expansion
normals
V'2
wave
2' must
be either
extensions
hodograph
curves
region
3 must of the
and
lies on a characteristic
of conditions,
being
extensions
plane
these
sets
any
point
from
flow field
end
end
(since
a iump
V2
the flow field 3 is separated form, of the initial Mach
2 through
if the
Similarly,
since
can
of
the
be used
to
waves
advancing
of solution
is
now
required. 259
TURBINE
DES,IGN
Consider Sa.
The
wall. P_
the flow
5 cannot The
because
in field wall,
in field
hodograph the
flows
According
one
that
wave
4 and
As
seen
from
the
Mach
waves.
across
the
used
in the
wave
stream
and,
the point
line
OP4,
Also,
P_
is, C_ or C'3.
these
conditions
diagram,
wave.
In
where
general,
an
as an expansion of the channel
net.
flow for
the
summarized
are
shown
along
(c) show
properties
are found
found
known
at the are,
method" in reference
design
of supersonic 9-10.
the
for
most
will 1.
not
Flow
each
waves,
and
the
because of the higher the reflected wave.
Mach
9-10(d)
boundary.
in the
same
produced without
shows A bend
direction by
and
the
wave.
any
additional
cancellation
at the
proper
of the
The
same
points,
situations, further.
as others blade
that
9-10(a), expansion of an
associated
location
(b),
and the
expansion
magnitude
boundary
conditions
(reflected)
waves.
as the are,
the reincident the
wave
top
wall
flow
is
wave,
with
expansion
in the
are
situation
In figure 9-10(c), angle than is the
of an
are
sections,
physical
reflection
number
the
or
procedure,
discussed
Figures
and
wave across
Figure
rotor
of a weak
respectively. smaller Mach
this
or lattice
the
cases
from a solid boundary, wave is at a slightly
regions,
practical be
"field
Solutions
case,
wave flected
through-
"lattice-point
In
as well
solution.
discussed
the
intersections,
stator
For
as
the form
the
in small
problems.
discussed,
hodograph
of expansion
finite
satisfied
flow
of
are
in
is called
previously
figure
quadrilaterals satisfied
may
in each
of procedure
of Elementary
previously
intersection
are
channel
regions
approximately
solutions
with
the
are
methods
"lattice-point are described
in
of the
procedure,
Summary The
sides
in supersonic
Both
in the
type
This
calculation
properties
Mach
The
flow
quadrilateral
of motion
stream
used
the
of small
therefore,
field.
the
identical. The Both methods
260
before,
hodograph
discussion,
equations
is often
the
foregoing
flow
Another
method,"
fied
of
that
a solid boundary reflects of the flow in the interior
is constant.
The
since
fields.
solid
field
therefore,
direction.
Ps,
is an expansion
by a number
entire
method,"
used
and,
same
segment
it from
extension
in the
to those
wall
Therefore,
separate
wall the
through
as shown P6
wall.
6 must
on
6 are
similar
P5 and
velocity
each the
the
lie
to the
the
as before.
which
of
field
characteristics
P8 be located
be approximated
out
to
to the
must
in fields of the
expansion wave striking wave. The construction proceeds
a new
6 is parallel plane
between
is parallel
parallel
and
to arguments
require
4, which
5 is not
the
flow
lie on
the
flow
APPLICATION
in field
extend
in the
must
AND
flow
at
is made deflection
therefore,
satis-
a
SfUPE./_SONI_C
Figure section point istic
9-10(e)
shows
the
of an expansion representing curves
continues
for the
and
a compression
wave
region
passing
solution D must
through
unchanged
lie on
B and
in type
flow field
the
the
beyond
wave.
The
intersection
C, as shown.
beyond
TURBINES
the interhodograph
of character-
Therefore,
each
wave
intersection.
6
(al 6
OD
BA
/
b
?//'//_}i"///d
;:P; ;,, .¢;
; ;4,:,_/_
_c_
(a) (b) (c)
Reflection FlovRs
Weak
expansion
Intersection of an
expansion
9-10.--Elementary
of
wave.
expansion wave
waves.
from
a solid
flow
solutions.
boundary.
261
TURBINE,
DESIGN
AND
APPLI_ATrON
6 It//l.I//l/l_'//.ft/lllll_ A
t
"V/I/i/////
0 B : 04 - 6
L
6_ (dt
Z////////21//7_
_-B
/---_1'--Compression wave
O0 : 0A + 25 "////Z ////I/I_
(e)
P : Constant
A
wave
_on
(fl
(f)
(d)
Cancellation
of expansion
wave
(e)
Intersection
of
and
Reflection
of
expansion
expansion wave
FIGURE
A case sections,
that but
This
is the
free
boundary.
262
is not may
be
from
a
at
boundary
the
design
in
interest,
of an boundary
waves. (constant
pressure).
9-10.--Concluded.
of general
The
boundary.
free
encountered
reflection
solid
compression
expansion condition
of supersonic
is shown
wave
from
requires
in figure
blade 9-10(f).
a constant-pressure that
the
pressure
be
SUPERSONIC
constant
along
velocity
the outside
magnitude
be equal.
Therefore,
In general,
field
wave
as a compression
DESIGN One
of
the
most
at
dimensional has
speeds.
to have
uniform
design
of a stator
based
Nozzles A supersonic in figure sonic,
9-11.
the
(DE), Point
that
(M----1).
Because
line
may,
and
Therefore, The
the for
flow
on this
that first
AD
generates
The
calculation
the
the
flow
plane. (constant
to produce of
of nozzle
Uniform
design
This
type
blades, the
will
uniform,
outward
(AD)
at
the
nozzle
throat
purposes, of the
and
ABCDA
is called
expansion
the
waves
is the
the here.
curve
super-
in again
to the initial flow. slope. It is usually parallel,
by
is shown and
and
sonic
axis is a streama solid
boundary.
be designed. expansion
which
same
flow
then
the nozzle
need
it is
Only
be parallel
be replaced
nozzle
since
Flow
is uniform,
symmetry,
two-
of nozzle
rotor.
parallel
flow
parallel of
be discussed
Parallel
the
uniform,
the
stator entering
that
of characteristics
tunnels.
flow type
BLADES
the wall is again parallel the wall has its maximum
design
procedure
the must
hodograph
method
basis
wind
produces
curve
one half
region
wall
is
parallel
it is required
of the
only
of
of a channel This
so that at the exit, D is the point where
assumed
uses
Producing
nozzle Since
wall must
in the
a free boundary
to supersonic-turbine
desired
is isentropic,
the boundary
STATOR
for supersonic
application
from
flow
along
be as shown
SUPERSONIC
to the design
nozzles
the
lying
reflects
important
supersonic
Since
fields
wave.
OF
is its application
also
C must
an expansion
pressure)
flow
streamline.
of all the flow
TURBINES
as was
reflect
zone. off
discussed
The
the
curved
centerline.
in the
section
[
B
FIGURE
9-11.--Supersonic
¢
nozzle
producing
uniform,
parallel
flow.
263
TURBINE'
"Flow
DE,SIGN
Between
ing section, in the
flow
past
for A
with
form
points
A
(corner
flow),
parallel that
one
at
of the half
wall
bounding _,
A computer with
Only
the
The
input
number output 3 does
flow
waves
that
waves
Mach
A
may
and
2 is set
long
form
of
been throats
ratio
coordinates for
any
_
the
of the
flow, the
to the
Prandtl-Meyer angle
of
the
working The
shows
corner
3) to design
includes
uniform
Therefore,
method
nozzle.
centerline.
to obtain
is designed
7 of the
of the flow
(ref.
edge
waves.
equal
nozzle
program
specific-heat
account
by
of the
the
Prandtl-Meyer
written
where
sharp
(fig. 9-12(b))
as a result reflected
It is a
9-11),
the by
used
9-12(a),
length.
(fig.
diagram
exit
figure
around
reflected
at an angle design
in
possible
is again
occurs
computer
shown
are
of the
portion
A,D
_.
supersonic
characteristics. by
the
desired fluid.
program
program. exit
The
of reference
losses.
[
_,_
3
/ _,5" ] 181
Physical FIGURE
I1);
plane. 9-12.--Nozzle
Mach
program
I
264
D.
be too
a limiting
previously
expansion
has
to the
(a)
was The
final
between
cases,
shortest
hodograph
program
the
these
incoming
Solutions."
type
expands
waves
The
sharp-edged
gives not
of this
described
of the
the
the
The
occurs
throat, in the
The
is half
supersonic and
Flow
supersonic.
In
as a result
region
which
nozzles
exit.
half
the
nozzle
reflected
the
other
and angle
the
coincide.
of the
flow
and
a nozzle
flow
producing
Cancellation
so that
straighten-
of cancelling
expansion
sharp-edged
parallel
D
method
applications.
a
of
and
is curved
the
is used.
uniform,
limiting
much
numbers,
turbine
nozzle
The
is called
of Elementary
parallel,
how
DCED
section
cancelled.
Mach
of nozzle
produces
in this
region
"Summary on
exit
type
The
is uniform,
supersonic
this
are
depends
large
wall
section CE
number
APPLICATION
Walls."
the
waves
seen
For
Two
and
expansion
AND
(b) Hodograph with
sharp-edged
throat.
plane.
SUPgRSONIC
The for
the
tional
sharp-edged-throat design
Stator
Nozzles
nozzle
just
of minimum-length
considerations
discussed
(chord)
for a stator
serves
supersonic
as compared
to the
TURBINES
as
the
stators. nozzle
basis Addi-
previously
Ideal nozzle -_ t
/ / /
Displacementth ickness-,
/
\ \ \
/
/
Straight sectior_ angle /_ozzle
/ Diverging section-'-.
/ /
/ /
Tangential direction
t_
Converging section-_ \
Axial _Trection
FIow_
FIGURE
9-13.--Design
of supersonic
stator
nozzle
with
sharp-edged
throat.
265
TURBINE
D_IGN
discussed
are
energy
AND
the
APPL_CATrON
flow
turning
A supersonic-turbine discussed
a stator
flow.
the
section
The
stream
suction
determined
sonic
by the
nozzles,
of the
type
the
nates
is first
are
then
local
rotors
OF
methods are
that
discussed
characteristics.
The
caused
entering
by
the
the
rotor
by
entering surface
of the
of
cancel
the
incoming
zontal
flow
(0=0)
corner-type
flow
The
expansion,
with
the
by
ideal
methods
obtained nozzle
by
coordi-
is obtained 7 (vol.
from 2).
BLADES
the
design
methods
use
of supersonic the
any
compression
method
shock
waves.
to be uniform
rotor
type
blades
is shown
(region
I)
along
the
and
of
forma-
The
flow
parallel.
waves. This
waves
concave surface In
parallel being
is given
in figure undergoes
(suction)
compression is obtained.
momentum
in chapter
for
in
dashed
Method
flow upper
by the
profile
to prevent
supersonic
from
is
is presented
efficiency
design
is assumed
parallel
blade.
to
proposed
convergence
resulting
length
super-
is then
ROTOR
is designed
of this
the
of characteristics.
ideal
profile
The nozzle
Both
blade
uniform,
compression,
the
as described
herein.
of designing
1). A typical
method
thicknesses
Corner-Flow One method
freesection
its
thickness,
final
channel passage
the
by
straight and
the
of
desired
indicated
the
for
The
been
the
for losses,
SUPERSONIC
have
by
losses,
of sharp-edged-throat
(displacement
9-13.
designed
is designed The
a
section,
turning
to
profile,
profile,
designed
parameters
DESIGN
flow
a correction
computed
in figure
of the
section
design
2).
(1)
converging
to minimize
nozzle
nozzle
displacement
as indicated
be
can
to
angle.
the
6 (vol.
boundary-layer
Two
for
sections:
and
discussed.
the
nozzle
(no loss)
in chapter
adding
266
and
be referred
The
the
as previously
parameters
etc.)
discussed
(ref.
flow
(supersonic)
all
This
will
surface.
order
produce
exit.
section
of three
speed In
to
including
9-13,
Boundary-layer thickness,
2).
the
required
4. An ideal
in figure
sonic
completes
program
stator
reference
suction
accelerates
at
surface
A computer
a diverging
to
section
of characteristics
the
tion
include
and
the
5 (vol.
number
channel
(2)
is designed
diverging
Mach
method
the
to
9-13
consists
on
flow
and
nozzle
section,
of chapter
converging
lines
desire
in figure
stator
section
accelerates
methods
on
The
a straight
section
blade
is shown
(subsonic)
(3)
the
stator
herein
nozzle.
converging and
the
losses.
being as
and
region flow
cancelled
by Shapiro 9-14(a).
The
a comer-type lower
(pressure)
is curved 2, then by
so as to
parallel
hori-
undergoes the
concave
a
SUPERSONIC
surface,
until
at the
blade
to the
inlet
For the tion
uniform exit. and
needs
of comer
since
only
diagram 9--14(c) quite
flow
blade
of one
kind
because
the
drawback
This loading
zero
upper
number
in any region.
one
in the
middle
half
of
The
specifica-
easy
to design,
The
hodograph
figure 9-14(b). Shown velocity distribution,
is that
parallel
profile.
only
particularly
distribution
occurs
surface,
the blade
9-14(a)),
of blade
of velocity method
Mach
it is symmetrical.
are present
becomes
of this design
in fig.
is shown in blade-surface
type
on the
since type
desired
complete
shown
this
for this blade is the theoretical unusual.
segments
(as
makes
of the
directions,
to be designed,
flow
waves
flow
Straight-line outlet
an impulse
blade
parallel
TURBINES
in figure which is
is not
very
of the
blade.
Another
inlet
Mach
number,
for a given
desirable,
rParallel flow I
t t
Parall
,_
Parallel flow -_ (a)
M*
Inlet
Outlet Distance alon9 chord
_b)
(c) (a)
(b) Hodograph
Blade
and
passage.
diagram.
FIGURE 9-14.--Supersonic
(c) Blade rotor
design
by the
loading
corner-flow
diagram method.
267
TURBINE
the
I_ESIGN
amount
sonic
(Mach
is limited.
1) or higher.
equal
to the
reasonable
turning
APPLICATION
of flow turning
therefore, For
AND
The
sum
Mach
inlet
levels
(120 ° to 150 °) would
method 5. This
the passage.
In a vortex-flow
critical out
shown
ratio
field.
A typical
in figure
The
(1.5
arcs
passage
inlet
the
by
field sect.
begins where The concentric
The
outlet
cular
arcs.
by
are
any
bution
to be quite
outlet,
program
input and
The
output
the
blade
shape.
without
locations
includes using
circular
of turning.
the
inlet
the
the
the
of on
blade
the
to the
hodo-
amount arcs
velocity
figure
the
9-15(a). the
circular
surface
especially
rotor and
can
distri-
9-15(c).
This
as compared
of
of this
to the
type
6. The
outlet
angles,
blade
method
blades
in reference and
rotor
method
figure BF
figure
with
9-14.
numbers,
approximate
and
cir-
parallel
in
shown, arcs
IK
the
and
is no limit The
by profile.
in
interflow.
uniform
is shown
diagram,
loaded,
into
blade
are
because
blade-loading
vortex-flow
surface
design
there
waves gener-
waves first the vortex
circular
rotor,
in figure
the
arcs
of design,
highly
The
indicated the
tranat the
waves
flow
upper
of
inlet flow
generated
surfaces
is presented
Mach An
the
for designing
includes
surface
gas.
268
shown
of characteristics
program
is
transition
compression
vortex waves
type
in the
the
The
expansion
complete
along
degree
on
design
A computer method
throughmethod
parallel
9-15(a)).
the
blade
the
type
arcs.
and expansion turn and maintain
this
the by
this
fig.
on
the
flows
necessary
is seen
corner-flow
(see
inlet
the
the
remaining
for to
of
and
directions
obtainable
is shown
blade
arcs
flow
along
In
turning
provide
within
therefore,
this
(1)
uniform
means
reconvert the
represented
transition
arc
segments
outlet
flows
diagram.
of flow
by
parts:
the
by arc
arcs
constant-velocity
graph
flow
(also,
is a constant
designed
three
outlet
the compression circular arcs
diagram
The
surfaces
radius
convert
flow
Straight-line and
of
transition
corresponding
The
of flow
is described
vortex
of velocity
passage
transition
cancelling
A hodograph letters
and
(3)
vortex
transition
to the inlet
9-15(b).
and upper)
upper
flow
amounts
blades
on establishing
the product
essentially
lower
ated
parallel
rotor
and streamline blade
and
into
by the
large
is,
angles.
Method
is based
arcs,
(lower
generated
turning
Prandtl-Meyer
to 3.0),
supersonic
field,
M*)
consist
(2) circular
sition
of flow
exit
be
9-15(a).
blades
arcs,
method
velocity
the
amount
2 must
be impossible.
of designing
in reference
in region
and
Vortex-Flow Another
velocity
maximum
of the
number
The
the
flow
specific-heat
by
computer the ratio
inlet, of the
coordinates
and
a plot
for obtaining
the
transition
characteristics
is
the
described
of in
SUPERSONIC
TURBI_,ES
references 7 and 8. In this procedure, the vortex flow is established by making the curvature of the transition arcs one-half the curvature of the circular arcs. For very small curvatures, this method is correct. In this blade design, the lower- and upper-surface Mach numbers are specified. This permits blades of various shapes to be designed for
Region Vortex flow transition
AB and FG BC and EF HI and KL CDEand1JK
Straight lines Upper transition arcs Lower transition arcs Circular arcs
(a)
M*..- _H,B
C
E
L,G
A,H
X'x// )
\
/ I
K
Inlet
Outlet Distance along chord
mh_7,F (c)
Ib) (a) (b)
Hodograph FIGURE
Blade
and
passage.
diagram. 9-15.--Supersonic
(c) rotor
design
Blade by
the
loading vortex-flow
diagram. method.
269
TURBINE
I_E,SIGN
AND
APPLICATrON AA AB BD CC CD
k
Circular arc Uppertransition arc Straight line Circular arc Lowertransition arc
\ D/
(b!
ta)
A A
A
B
B
Lower-surface
Prandtl-Meyer
an-
gle, 0° (M = 1) ; upper-surface Prandtl-Meyer angle, 59 ° (M = 3.5) ; total flow turning angle, 130 °. (c) Lower-surface Prandtl-Meyer angle, 18 ° (M---- 1.7) ; upper-surface Prandtl-Meyer angle, 59 ° (M = 3.5) ; total flow turning angle, 130 ° . (e)
Lower-surface Prandtl-Meyer angle, 21 ° (M-- 1.8) ; upper-surface Prandtl-Meyer angle, 59 ° (M---- 3.5) ; total
flow
turning
FIGURE 9-16.--Turbine Meyer 270
B
A B
A
D
D
(a)
B
angle,
120 ° .
(b)
B
Lower-surface Prandtl-Meyer angle, 12 ° (M=l.5); upper-surface Prandtl-Meyer angle, 59 ° (M = 3.5) ; total flow turning angle, 130 °.
(d)
Lower-surface Prandtl-Meyer angle, 18 ° (M----1.7) ; upper-surface Prandtl-Meyer angle, 104 ° (M----10.7) ; total flow turning angle, 130 °. (f) Lower-surface Prandtl-Meyer angle, 21 ° (M---- 1.8); upper-surface Prandtl-Meyer angle, 59 ° (M = 3.5) ; total flow turning angle, 140 ° .
blade shapes at inlet Mach angle of 39 °) and specific-heat
number of 2.5 ratio of 1.4.
(inlet
Prandtl-
SUPEJRSONIC
a given
inlet
program
Mach
of reference
figure
9-16.
From
number
(cf. figs.
whereas
the
(c))
number.
and
effects.
the
9-16(c)
(cf.
in
will
of which
the
flow
for
program
for the design
including
a correction
(no loss) eters ing
passage
designed are then
in figure
the
of
later
case
computed,
indicated
final
Rotor
loss
profile
parameters
.... _--
shape, (b),
and
significant
is obtained
starting
by
problems,
characteristics" flow.
dashed
lines
design A computer
rotor
in reference
to the
is then ideal
in figure
_
._ --'__/'x
"
/__/
_,.
i/
9-17,
is
by
add-
as indicated
are determined 7 (vol.
ideal
param-
obtained profile
in chapter
sections,
9. The
Boundary-layer
profile
as described
blade
have
vortex-flow
coefBcients
in
chapter.
of characteristics.
and the
(f))
(isentropie)
by the
the
Mach
9-16(a),
design
of
is presented
thicknesses
boundary-layer
in this
of ideal
displacement
9-17.
and
of supersonic-turbine
the method
on the
figs.
supersonic
"method
by
upper-surface
effect
a blade
and
for losses,
profile,
by
the local
selection
designed
of 2.5 axe shown
the
(cf.
9-16(e)
separation
discussed
is only
number
has little
figs.
blades
that
number
be discussed
previously
Mach
(d))
flow
both
first
and
turning
of
it is seen
Mach
of
procedure
figure,
lower-surface
Guidance
number
6 for an inlet the
consideration The
A
_URBINES
from
the
2).
Displacement thickness
_
,--Loss-free
passage
\
Z
\
\
FIOURE
9-17.--Design
of supersonic
rotor
blade
section.
271
TURBINE
As
DESIGN
seen
from
transition
arcs
results
severe
in large
of the
upper-
9-15,
and
OPERATING
the flow
exist
along
passages.
The
of whether
places
Mach
blade
separation.
it would
criterion
lower-surface
gradients
rotor
an indication
to cause
If it is possible,
separation
and
pressure
within give
enough
losses.
The
adverse
EF
calculations
are
separation.
APPLICATION
figure HI
boundary-layer gradients
AND
the
Flow
be desirable limitations
pressure
separation to prevent
on
the
choice
numbers.
CHARACTERISTICS
OF
SUPERSONIC
TURBINES Supersonic
the
Problems diffuser
Starting
occur in the starting must be able to swallow
of supersonic the shock that
diffusers because forms at the inlet Lowe r-s u rface PrandtI-Meyer angle,
140
o)/, de3 ,/_---
120
120 ll5 llO 105 9O 85 8O 75 7O 65 6O 55 5O 45 40 3O 75 2O 15 10
___------------
20
0
t
1
20
40
1 60
Upper-surface
FIGURE
9-18.--Maximum
272
1
I
I
l O0
120
140
starting.
Specific-
Prandtl%_eyer
Prandtl-Meyer heat
t 80
angle ratio,
1.4.
an(jl¢,
for
'%,
supersonic
deg
SUPE_
during
startup.
in shape,
Since
similar
of supersonic
turbines.
a normal
shock
ing.
permissible
The
condition, wave
Mach
flow
can
this rotor
blades
angles.
(often
angles
w_ and
(or inlet
established. value
the
must
the then
wz), there
starting
instant
passage
enough
that
of start-
is set
to permit
by
the
velocity
circular-arc of
this shock
diagram,
and
the
order
to
determining the
maxi-
of vortex-flow
blade-surface inlet
of the
supersonic
9-18,
starting
the
in
value
for
6. In figure
of the
of
corresponding
for which
procedure
problem,
determined
segments
the
a maximum
angle)
for supersonic
as a function design
be
exists
in reference
angle
the terms
calculation
is given
usual
from
in
Prandtl-Meyer
The
is plotted
In
at the
blade
along
expressed
Prandtl-Meyer
is known angles
numbers
the
be large
in the
it is assumed
passage
of
Mach
to occur
approximation,
blade
must
flow
maximum inlet
a first rotor
contraction
number
mum
is convergent-divergent
be expected
passage
surfaces
be
passage
TURBINES
through.
Prandtl-Meyer inlet
blade
would
the
the
specified
blade
rotor As
spans
since
to pass
For the
the
problems
SONI_
Prandtl-Meyer
Prandtl-Meyer
angle
surface
Prandtl-Meyer
obtain
the
rotor
blade
8O
-
k
Lower-surface Prandtl-Meyer angle,
E
_
_o
&
39
r_
•_
I
4o
g &
c 5
__e_,
o,io, S9 0
F_,...'_, ,//
,
7" ,'_7,_97._/'/77"7"//'77/'I
,'
,
,
,/
'
,
/,
20
E
I
I
r_
o
l_°l
i_oo
I lJ
1
_
50
30
l 70
L
I
,,
90
I 1 110
Upper-surface PrandtI-Mever angle, wu, deg FIGURE 9-19.--Supersonic Mach number 2.5;
inlet
starting criterion Prandtl-Meyer
applied to example angle, 39°; inlet flow
turbine. Inlet angle, 65 °.
273
TURBINE
and
DESIGN
passage
AND
profiles.
conditions,
the
in figure
APPLICATION
To
point
9-18
must
assure
representing
the
lie on or above
the
inlet
Prandtl-Meyer
angle.
tion
places
restriction
surface
a severe
Mach
Suppose
numbers. a
(1) _=1.4;
blade
is
noted
that
39 ° to 104 °. The
must
remain the
at
inlet
shown.
be
would starting limit
than
indicated
the
limit
the
ported
in
efficiency
not
be
in the
velocity ratio)
efficiency rapidly
as
to that efficiencies
pressure (circles
for
14.
at ratio
in fig.
a subsonic at
curve.
the The
ratio
(blade
angle
Prandtl-
this
example.
design
purposes
are
region
shown because
consideration lower values
If
For
pressure
ratios
divided
were
the
data
ideal
for
given
ratio
and in
have
the
speed, falls
off
maximum
ratio
a subsonic
in supersonic-turbine
by
any
speed
would
re-
exit-static-pressure
variation
blade-jet
are
supersonic-turbine
presents
The
this
turbines
speed
14.
design
with
pressure
in
to
which
decreased.
9-20)
decrease
flow
the
inlet-total-
reference
turbine.
lower
variation
about is
fact
inlet
°, and
supersonic
The
9-20, of
the
Performance for
turbine
turbine
is maximum
efficiency
274
to
flow
previously
Flow separation value of w_ to much
data
in figure
for
vary
the
figure.
speed
corresponding is illustrated
of _,
for
to
inlet
discussed
_,=39
Turbine
to
blade-jet
partial-admission
envelope
10
the
°.
_, can that
maximum
_,
permissible
that fact
w, is due
exceed the
conditions:
(3)0,.----0,_=65
to the on
of
an example.
following and
condivalues
from
0 ° to 39 °, and
9-19,
considerations. the maximum
design
seen
the
_z is due
w_ and
represents
performance
with
for
to the
starting
permissible
as a function
line
references
corresponding
is best
cannot
of
Supersonic Experimental
angles
supersonic
104 ° limit
In figure
bounds
of supersonic will, in general,
the
from on
is plotted
dashed
crosshatched
vary
turning
the
Prandtl-Meyer
ordinate the
designed
sonic;
w_,. ,,_
The
can
104°).
only
given inlet
(_,.=_,x=39°);
transition
angle clarity,
surface
restriction
0 ° limit
least
of 65 ° (39°+65°= For
to
_
from
Meyer
on
This
for the
starting
In general,
(2) M,,=Mex=2.5
It is first
that
satisfactory
is similar turbine,
the
fallen
on
the
efficiency
at
the
8UPF_R_)NIC
TURBII_S
Ratio of turbine-inlet total pressure to turbine-exit _
a
static pressure 150
o o
120 63 (design)
_
"_
_
I
.30
cCD
.2O _3 t_
.10
....... 0
F,GuR_.
L__ ......... 2___ .04
9--20.--Static
.08
efficiency
The
1 .16
of turbine as function for conseant speeds.
lower pressure ratios is due expanded
A_ .12 Blade-jet speedratio
to
J
l
.20
of blade-jet
.24
speed
ratio
the shocks occurring in the under-
stator nozzles.
variation in static pressure throughout
the turbine of reference 14 is shown of the shock waves
the stator nozzle of
in figure 9-21. The
in the underexpanded
formation
nozzle is readily apparent.
It can also be seen from this figure that at pressure ratios near design, the divergent section of the nozzle performed pressure did not remain
as expected, but the
constant in the straight section. There
some overexpansion followed by some compression. havior was found in the data of reference 10.
This
same
was be-
275
TURBINE
I_E_IGN
AND
APPLICATION
• 10-__
Divergent -section
Straight .... section
["-
I
•09 --
.0_
•07 -a
c
9
•05 -L_
V o
•03 --
A •02 -[] Theoretical .01 -Throat I
Exhaust
Ii
i
.2
.4
It .6
L
_
.8
1.0
Fraction of axial distance FIGURE for
276
9-21.--Variation constant
of ratios
nozzle
of nozzle
pressure exit
static
ratio pressure
with to
axial inlet
distance total
in
pressure.
nozzle
SUPE_tSONIC
TURBINES
REFERENCES 1. 2. 3.
4.
5.
6.
7.
8. 9.
10.
11.
12.
13.
14.
ASCHER H. : The Dynamics and Thermodynamics of Compressible Fluid Flow. vol. 1. Ronald Press Co., 1953. LIEPMANN, HANS WOLFGANG; AND PUCKETT, ALLEN E.: Introduction to Aerodynamics of a Compressible Fluid. John Wiley & Sons, 1947. VANCO, MICHAEL R. ; AND GOLDMAN, LOUIS J. ; Computer Program for Design of Two-Dimensional Supersonic Nozzle with Sharp-Edged Throat. NASA TM X-1502, 1968. GOLDMAN, Louis J.; AND VANCO, MICHAEL R.; Computer Program for Design of Two-Dimensional Sharp-Edged-Th_roat Supersonic Nozzle with Boundary-Layer Correction. NASA TM X-2343, 1971. BOXER, EMANUEL; STERRETT, JAMES R. ;AND WLODARSKI, JOHN; Application of Supersonic Vortex-Flow Theory to the Design of Supersonic Impulse Compressoror Turbine-Blade Sections. NACA RM L52B06, 1952. GOLDMAN, LOUIS J. ; AND SCULLIN, VINCENT J. : Analytical Investigation of Supersonic Turbomachinery Blading. I--Computer Program for Blading Design. NASA TN D-4421, 1968. STRATFORD, B. S. ; AND SANSOME, G. E. : Theory and Tunnel Tests of Rotor Blades for Supersonic Turbines. R&M 3275, Aero. Res. Council, 1962. HORLOCK, J. H. : Axial Flow Turbines: Fluid Mechanics and Thermodynamics. Butterworths, 1966. GOLDMAN, LOUIS J.; AND SCULLIN, VINCENT J.: Computer Program for Design of Two-Dimensional Supersonic Turbine Rotor Blades with Boundary-Layer Correction. NASA TM X-2434, 1971. MOFFITT, THOMAS P.: Design and Experimental Investigation of a SingleStage Turbine with a Rotor Entering Relative Mach Number of 2. NACA RM E58F20a, 1958. STABE, ROY G.; KLINE, JOHN F.; AND GIBBS, EDWARD H.; Cold-Air Per-
SHAPIRO,
formance Evaluation of a Scale-Model Fuel Pump Turbine for the M-1 Hydrogen-Oxygen Rocket Engine. NASA TN D-3819, 1967. MOFFITT, THOMAS P. ; AND KLAG, FREDERICK W., JR. : Experimental Investigation of Partialand Full-Admission Characteristics of a Two-Stage Velocity-Compounded Turbine. NASA TM X-410, 1960. JOHNSON, I. H.; AND DRANSFIELD, D. C.: The Test Performance of Highly Loaded Turbine Stages Designed for High Pressure Ratio. R&M 3242, Aero. Res. Council, 1962. GOLDMAN, LOUIS J.: Experimental Investigation of a Low Reynolds Number Partial-Admission Single-Stage Supersonic Turbine. NASA TM X-2382, 1971.
277
TURBINE
I)E_IGN
AND
APPLICATIO_
SYMBOLS A
flow
a
speed
g M
conversion
M*
critical
P
absolute
area
along
of sound,
Mach
wave,
m/sec;
mS; ft _
ft/sec
constant,
1;32.17
(lbm)(ft)/(lbf)(sec
_)
number velocity
ratio
pressure,
component
of
m/sec; V
Mach
lb/ft _
velocity
parallel
to
initial
flow
direction,
initial
flow
direction,
ft/sec
velocity, critical
V
component
Y)
mass
m/sec;
ft/sec
velocity
(M--
of
m/sec;
1), m/sec;
velocity
ft/sec
normal
to
ft/sec
flow
Mach
(V/Vc,)
N/m_;
rate,
angle,
kg/sec;
lb/sec
deg
ratio of specific heat constant volume
at constant
small
direction,
change
0
flow
p
Prandtl-Meyer
P
density,
in flow
angle,
pressure
to specific
deg
deg angle,
deg
kg/m 3; lb/ft 3
Prandtl-Meyer
angle,
deg
Subscripts e_
rotor
exit
in
rotor
inlet
l
lower
surface
ITI4IZ
maximum normal
direction
7"
relative
8
isentropic
t
tangential upper
278
of blade with
direction
surface
respect
with
of blade
to Mach
respect
wave
to Mach
wave
heat
at
CHAPTER 10
Radial-lnflow Turbines ByHarold E.Rohlik Radial-inflow space
power
turbines systems,
are suitable
and other
for many
systems
applications
where
compact
in aircraft, power
sources
are required. Turbines of this type have a number of desirable characteristics such as high efficiency, ease of manufacture, sturdy construction,
and
reliability.
radial-inflow
There
turbines
in nature
and cover
most
machines.
In this
chapter,
its
features
addition, design
flow
turning long 8.
Radial
with
a section
the flow
those
stator takes
In
through
radially place
axial
height
the varies
rotor
and from
stator
which
is a doughnut-shaped is a spiral
inlet.
torus
is fed inlet
axial-flow
and
turbine.
design,
In
and
off-
by pipe.
flow
the
rotor
passage, blade blades,
This
is relatively
ratio,
about on
turbine.
axially.
which
aspect
from
plenum,
passage,
a radial In
radial-inflow
1 to
the
which
is
as much
other
hand,
the
inlet case
or a volute
usually pipe,
surrounds while
of a volute,
the
(shown the
in
stator
volute
is fed
a prewhirl
(tan-
of velocity) is imparted to the gas before it enters row. This results in stator blades with little or no
It can be seen
radial-inflow
of these
0.1 to 0.5.
which
camber.
on
is described,
blade
leaves
turbines,
ratios
gential component the stator blade
an
a typical
and
A torus, The
of
to chord,
aspect
a tangential
performance
turbine
in the rotor
fig. 10--2), by
of information
1 to 6 are general
and
performance,
turbine
have
design
radial-inflow
and
of blade
generally
of the
the
amount References
are discussed.
narrow.
ratio
areas
geometry
shows
enters of the
and
the as
10-1
literature.
compared
performance
Figure The
are design
is a substantial
in the
turbine
from
figure
is considerably
10-2
that
larger
the than
overall the
diameter rotor
of a
diameter. 279
TURBINE
DE, SIGN
AND
APPLICATION
Station :,
0
Stator blade -
1 2
Rotor blaue
FIGURE
At little
the
rotor
or
no
usually
10-1.--Schematic
inlet,
generally
is rather
varies
where the
velocity
has
Figure shows solidity generally turbine blades 280
to
or no
shows
the
prewhirl
(ratio
of
used shown in the
of
turn
radius.
the
blading
the
stators
They
section
angular
blade
rV,
of absolute
V,,=U_r,
the
that
the
The
stator
(where
velocity)
W_=O, At
has are
rotor
momentum
(Since so
rotor blades
of the
rV,,a:r2.)
flow,
to the rotor
rotor
exit
exit,
absolute
whirl.
to
has
the
component
more
is developed
in
rotor.
since
turbine.
relative
straight
Therefore,
chord
here
velocity
tangential
square
of radial-inflow
(W_=O),
This
speed.
curved
little
10-3 that
the blade
are
flow
loaded,
V_ is the
with
U is the blades
radial.
highly
and
the
section
component
and
r is the radius, here
where
tangential
straight
cross
clearly.
in the
inlet
volute.
and
low
aspect
spacing)
of radial
splitter,
or
are
in the
used
turbines
partial, radial
blades part
blade Also, ratio
can
be
between of the
shape the
low
that
are
seen. the
The full
flow passage
RADIAL-INFLOW
TURBINES
Stator
/- Rotor /
Volute
C-72323
FIGURE
to reduce the the "BLADE The in
The
relative
radius,
an
axial
in a radial because
temperature
discussed
discussion).
turbine
because
overall
expansion.
diagram
process turbine
total
as was
associated
This
in figure
and
the
_hown
for
tile
p_'
line
fig.
2-8
only
of ch.
to rotor
2), losses.
to both
the
If
be only
this
the the
relative
were
an
below
losses
from and
the the
(2-31)
for
the
change
and radial
a given
the
turbine
p_'
line p['
rotor
temperature
pressure
as shown
p't' line
for
through total
axial
between
turbine,
decreasing
eq. level
total
the
rotor.
temperature-entropy
expansion
in
from
the
with
velocity
in relative
difference radial
removed rotor
the
change
slightly
because For
shows
in
1 (see
the
in
appreciably
advantage
from
further
change
decrease
of a lower seen
change
expansion.
would
use
Tile
corresponding
the
pressure
a distinct
be
which
turbine.
the p;' line is farther is due
10--4,
the
discussed
differs
radius
2 of volume
is
can
are
turbine
and
This
blades
of the
in chapter
it permits
of a radial-inflow T"
turbine.
blade loading. Splitter DESIGN" section.
expansion
that
10-2.--Radial-inflow
p" (T['=T_'),
(as and
shown p_"
in figure
because in radius.
are
the
in
is due 10-4,
difference Therefore, 281
TURBINR
I)F__SIGN AND
APPLICATION
Rotor splitter blade--
Stator blade--.
Rotor full blade
/
/
/ t
C-?1863 -
FIGURE 10-3.--Turbine
expansion
from
exit the
pressure exit in
static rotor
vertical
distance
friction
losses
the relative is clear. A
the
same
gas
U_ and the
increase
velocity,
the
velocity
approximately turbine. 282
Us is very relative three
total
assembly.
pressure
a higher than in
diagram inlet 0.5.
times
to
is shown
the
level
in
W= at (larger
figure
For
a typical
as high
W] if
zero-exit-whirl
leaving
U2 equaled
the UI,
rotor
fluid
square
of
of velocity 10-5
volute and a mean diameter The difference between the
energy
same
Since
with
of a lower
the
velocity turbine
turbine.)
approximately
advantage
evident.
kinetic
p'_'
relative a radial
p_" and p= for an axial
a rotor
turbine with prewhirl in the (exit-mean to inlet) of about diagram,
and rotor
inlet
p_ would require an axial turbine
radial-turbine
speeds
stator
rotor
between in
. _gak-
for
a
ratio blade
velocity would
as in an
be axial
RADIAL-INFLOW
TURBINES
i
T1
tl
2gJCp
TI
E
2gJcp
F--
Entropy FIGURE 10-4.--Temperature-entropy
diagram
for a radial-inflow
turbine
rotor.
V0
W]
W2 /
p2-.
U2 FIGURE 10-5.--Velocity
diagram.
283
TURBINE
DE'SIGN
AND
APPLICATION
OVERALL
Since
the
shown
blades
in figure
angle
that
provides
This
angle
blade.
This
in a centrifugal
of the
blade
Before
ferentially gradient the
that
the
point
when
separate sive cally
from
loss. and
The
so that pattern
is an
there
If
suction
relation
experimentally
properly
"optimum"
10-6.
angle
Note this
that were
surface
between in
FIGURE
the
near
the
10-6.--Streamline
with
the
unloading
flow
blades,
_1. This the
U1 has
compressors
toward
flow condition
inlet
stagnation is shown
stagnation
flow
would
edge,
causing
been
studied
and
turbines.
inlet.
rotor
it is circum-
pattern
/
flow at rotor
in the
shift
the
flow at the
"slip"
static-pressure
of this
locates
so,
;uction urface
to the
is a streamline
leading
V_._ and both
leading
a large
the
incidence a radial
rotor
not
fll
rotor-blade
of mass
produces
angle
as 40 ° with
is analogous
flow analyses
Pressure surface
284
by then
flow
is some
is associated
distribution
loading
passage,
radial. the
the
inlet
at the as high
condition and
the
There
conditions
Stream-function
in figure
is approximately
angle.
is influenced
streamline
inlet,
sometimes
and
Blade
the
there
schematically
tip flow
surface.
show
flow
a value
the
rotor
incidence
incidence
the
across
at the
compressor,
uniform.
suction
Incidence
is an
optimum
factor passage.
Optimum
optimum has
near
CHARACTERISTICS
are radial 10-5
edge.
DESIGN
point tend
to
excesanalytiIt
has
RADIAIr-INFLOW
been
determined
optimum
that
ratio
number
there
depends
and is often
is an optimum
on
blade
expressed
as
loading
V_"=1---2 where
n is the
number
of
ratio and,
TURBINES
of V,. 1 to
U_. This
consequently,
blade
(10-1)
U,
n
blades
(total
of full
blades
plus
splitter
blades). Effect The vol.
of Specific
specific
Speed
speed
1) is given
by
on Design
parameter the
Geometry
N_ (derived
and
and
Performance
discussed
in ch. 2 of
equation NQ21/2
N_--
(10-2)
H314
where N
Q2
rotative volume
H
ideal
speed, rad/sec; rev/min flow rate at turbine exit, work,
or head,
based
m3/sec;
on inlet
ft3/sec
and
exit
total
pressures,
J/kg;
(ft) (lbf)/lbm In
its
most
units), size
commonly
it is not and
be
and
Analytical examined
truly
may
geometric
by
used
form
(with
dimensionless.
considered
Specific
as
velocity-diagram
the
a
shape
stated
U.S.
speed
customary
is independent
parameter
that
of
expresses
similarity.
study.--The
effect
substituting
for N,
of specific Q2, and
N
=
speed
on efficiency
may
KUI
(10-3)
Q2=_-D2h2V2 H=Vj2
be
H as follows:
(10-4)
(hh'_
(10-5)
where K
dimensional
D1
rotor
D2
rotor-exit
mean-section
h2
rotor-exit
passage
V2
rotor-exit
fluid
m/sec;
ft/sec
v,
inlet
ideal
jet
ratio, g
constant,
conversion
(tip)
speed, m/sec;
2_ rad/rev;
diameter,
m;
velocity based
ft
diameter,
height,
60 sec/min m;
ft
m; ft (assumed on
to be in axial
inlet-total
to
direction),
exit-static
pressure
ft/sec
constant,
1 ; 32.17
(lbm)
(ft)/(lbf)
(sec 2) 285
TURBINE,
DESIGN
Ah_
ideal
AND
work
APPLICATION
based
on inlet-total
and
exit-total
pressures,
J/kg;
based
on inlet-total
and exit-static
pressures,
J/kg;
Btu/lb Ahid
ideal
work
Btu/lb These
substitutions
expression
for
and
specific
some
manipulation
result
in
the
following
speed:
y. N,=(Constant)\_-7]u The
terms
teristics by an
\-_j/
of equation
(10-6)
are
\U],
related
\D,]
of these
combinations
7 to determine
were
optimum
(10-6)
to velocity-diagram
and overall geometry. Any specific speed infinite number of combinations of these
number
\D.]2
examined
combinations
value ratio
charac-
can be achieved terms. A large
analytically
over
a wide
in reference
range
of specific
speed. The
analysis
of reference
properties,
neglecting
were
caused
those
shroud
clearance,
kinetic
energy.
exit
flow
the
stator
windage
on
number
to provide
This
was
the
tion
(10-1)
included
the
total
the
to establish
a maximum
limit
of
the
rotor, varied
blade-to-
and
the
with
(10-7) would
avoid
splitter)
angle. zero
and
exit
stator-
equation
plus
incidence
Dt.2/D_,
considered
layers,
was
that
(full
(W_:2W_),
of 0.7 for
flow
12
number
rotor
losses
the
to the
of blades
reaction
The
blades
(a_--57)_T
minimum
mean-diameter
boundary
back
according
number
a favorable
rotor
of rotor
al (in degrees)
to
variations. and
n:0.03 in order
losses
hub-to-shroud by
The
angle
7 related
separation.
used
Other exit
in equa-
assumptions
whirl
a minimum
(V_,2:0),
limit
of 0.4
for
(nh/D,)2. The
effects
examined number
of
height Vc,)_. fell
The
to be
region
for
set
by
geometric large values. 286
mentioned
combinations
of
stator-exit
flow
D,.2/D_
static
the
any
in static
angle.
is the
value
angle
The
against
as much
ratios
specific
falls
boundaries and speed, the
speed. points
flow
angle
into
a small
of each by
the there
as 45 to 50 points of all
(U/
calculated
Stator-exit
variables
a large
to rotor-inlet
velocity
which
were
for
stator-blade-
rotor-exit
of specific
envelope
a_,
all of the 10-7.
of input
given
efficiency,
curve
plotted
study,
of efficiency,
flow values
For
and
losses
critical
in figure
determinant
extreme
dashed
then
in the
shown
stator-exit
hdD_,
rotor-tip
was
used
areas
a prime each
three
efficiency
limits. The
ratio at
of values
shaded
variation
characteristics
previously
range
in the
velocity-diagram
the
ratio
the
seen are
and
calculating
to rotor-inlet-diameter
diameter For
of geometry
by
computed
is
region assumed can
be a
for some static
RADIAL-INFLOW 1.0
Total efficiency corresponding to curve of maximum static efficiency
Stator-exit flow angle, aI , deg
.9 _
TURBINE_
of maximum static efficiency
8
\ \
.7
\
8
\ \
.5
.4
.3
._ 0
.2
[
I
[
.4
.6
.8
t
I
I
1.0
1.2
1.4
Specific speed, Ns, dimensionless
l
I
I
I
I
I
l
I
I
I
0
20
40
60
80
lO0
120
140
160
180
Specific speed, Ns, (ft314)',lbm314)/(min)(secll2}(Ibf3t4) FIGURE
10-7.--Effect
efficiencies, total
of
and
the
efficiencies.
achievable
associated
with
primary mum
Most the ure
specific height creases
of that
study,
velocity
curves. of specific
10-8
specific
model
geometric
envelope
functions
shows
The
that and
speed.
Figure increasing
efficiency.
corresponding
do not
are
many
study was
necessarily assumptions
of reference
to determine
shows
specific
values
vary
7. The the
opti-
to a larger
flow flow
that
the optimum
is small
at low
speed
continuously
of some in figures
stator-exit
(opens
diameter
ratios
presented
optimum
10-9
there in the
velocity
are
decreases
to rotor-inlet
the
of efficiency
however,
optimum
the
it represents
values used
design-point
ratios. and
speed
speed
with
above because
loss
and
of the
curve
computed values,
the
concern geometry
solid
The
represent
specific speed on computed (Data from ref. 7.)
until
of 10-8 angle
area) ratio
specific
a maximum
these
along ratios
to 10-11. is large with
as Fig-
at low
increasing
of stator-blade speed
and
in-
is reached
at 287
TURBINE
DESIGN
AND
APPLICATI.ON
90-XD
_" 8O
¢D
_o 70
60
I
5O .2
.4
.6
.8
1.0
1.2
1.4
Specific speed, Ns, dimensionless
l
1
I
I
I
I
t
1
I
20
40
60
80
i00
120
la3
160
180
Specific speed, Ns, (ft3J41(Ibrn3/4)/IminJlseclJ2jIIbf3/4_ FIGUaE
10-8.--Effect
of specific speed on optimum (Data from ref. 7.)
stator-exit
angle.
Blade critical velocity ratio at rotor inlet, • 20 --
(UtVcr)l 0.20
O
oA XZ
L_"
_z u_
C
0
0
a:
.08
.04
0
I .4
.2
I .6
1 .8
[ 1.0
I
l '1.2
l.a
Specific speed, Ns, dimensionless
I
I
I
I
I
I
J
I
I
20
40
60
80
l O0
120
140
160
180
Specific speed, Ns, (ft3/d_tlbm314t/Imin!lseclIZJ_lbf3i4_ FIGURE
288
10-9.--Effect of specific speed blade height to rotor-inlet
and blade diameter.
speed on optimum (Data from rcf.
ratio 7.)
of stator-
RADIAL-INFLOW
TURBINES
.l E 7-
.6 O
.4
--
¢_
.o f-f
I
.2 0
.2
.4
.6 Specific
I,
I
0
20
I 40
I
I
I
I
.8
1.0
1.2
1.4
speed, Ns, dimensionless
I
1
60
80
I
I
I
I
I
100
!20
140
160
180
Specific speed, Ns, (ftJld}(Ibm3/41/(min_secll2)ilbf314_
FIGURE
10-10.--Effect diameter
14
specific
speed
on
diameter.
optimum (Data
ratio from
ref.
of
rotor-exit
tip
7.)
--
L
I
0
FIGURE
of
to rotor-inlet
20
10--I
1.--Effect
of specific (Data
speed
on optimum
from
ref.
blade-jet
speed
ratio.
7.)
289
TURBINE.
some
value
in the mum
DESIGN
AND
APPLICATION
of specific
speed
turbine.
The
only
geometric
and
velocity
it is seen blade
that
height
Figure
10-10
higher to
depending
effect
shows
that
ratios
velocity the
level
any
ratio
of velocity on
in figure
in smaller
at
optimum
has
shown
result
diameter
that
overall
compressibility is also
levels
rotor-inlet
on the
the
10-9,
ratios
given
optiwhere
of stator-
specific
of rotor-exit
speed. tip
diam-
[]
qb_
(a)
Specific
speed,
0.23;
30
(ft
3/_)(lbm
flow (b)
Specific
speed,
0.54;
70
(ft
3/_)(lbm flow
(c)
Specific
speed,
1.16;
150
290
10-12.--Sections
of
_tZ)(lbf
3/_). Stator-exit
l!Z)(lbf
air).
Stator-exit
l/2)(lbf
3/4).
Stator-exit
81 °. 3/_)/(min)(sec
angle,
(ft 3/_)(lbm flow
FmURE
3z_)/(min)(sec
angle,
angle,
radial
turbines
(Data
from
75 ° . 3/4)/(min)(sec 60 ° . of ref.
7.)
maximum
static
efficiency.
RADIAL-INFLOW
eter
to
rotor-inlet
creases
rapidly
diameter with
of D,2/DI_-0.7 optimum
is
is reached.
blade-iet
to the
variation
The
optimum
values
shown
design
of radial-inflow
geometries These
are
shown
sections
that
varies
of static
10-12
figure with
10-8
and
imposed
10-11
inlimit
that
specific
to 10-11
Sections
specific
speed
the
the
speed
in a
efficiency.
in figures
in figure
show
specific until
from
UI/Vj
turbines.
low
speed
is seen
ratio
similar
at
specific It
speed
manner the
small
increasing
TURBINE_
for three speed
can
of turbines values
be used
with
of specific
is largely
an
for
optimum
index
speed. of
flow
capacity. The
design
different
study
losses
shown
in figure
values
of specific
.2
1.0
of reference
along
the
10-13
7 also
curve
for
the
speed,
the
indicated
of maximum range
stator
the static
efficiency.
of specific
speed
and
viscous
rotor
variation
in the This
covered.
For
losses
are
is low
very
--
.9-p
¢x3
to
¥ Loss Stator
c <19
Rotor Clearance
:>
Windage Exit velocity
c_
I
.4
,
.4 Specific
1
_ Specific
10-13.--Loss
.6
.8
I 1
2
speed, Ns, dimensionless
n
_0
FIGURE
1 , 1,1,1
.2
J 50
I
1
J
80
100
200
speed. Ns, l[t3_'4Jllhm3/d_/fi:lin_secll2_ltbf3'4_
distribution
along (Data
from
curve ref.
of
maximum
static
efficiency.
7.)
291
TURBINE,
large
DESIGN
because
of
clearance
loss
relatively
large
which large
the
APPI_CATION
high
is large on specific
speed increases, loss all decrease kinetic-energy
of
primarily speed
the stator because loss
ratio
of wall
because
fraction
depends at low
AND
the
passage
area.
the
diameter
and
of the
The
the
flow
is
windage
rotative
low
Also,
clearance
height.
and rotor losses, of the increased
becomes
to flow
blade-to-shroud
the because
area
speed, rate.
As
a
loss, is also specific
clearance loss, and windage flow and area. The exit
predominant
at
high
values
of
specific
speed.
C-/I-159
C-69q816 {a)
ib_
C-?0-3533 to)
(a)
Design
rotor.
(b) (c)
FIGURE
292
10-14.--Rotor
configurations
Cut-back used
Rotor
with
exducer
extension.
rotor. in
specific-speed
study
of reference
8.
RADIAL-INFLOW
Experimental
study.--In
effect
of specific
(ref.
8) to accept
of
blades
and
extension stator
the
turbine
rotor
back.
Details
calculations Performance
from a large with
the
was
area
area over
and
range the
rotor
rotor
was
was
also
with
to
results,
the
area
and
allowed
the
This
and
in-
vary
throat
speed.
an
for
Figure
extension,
10-14 and
internal
cut
velocity
8. experimentally
area.
numbers
back
used
design
of specific
modified
fitted cut
were of the
the
was
different
reduced-area
test
in reference determined
with
53 to 137 percent.
geometry,
given
The and
modifications
as designed, of
are
angles.
experimentally a turbine
rows
20 to 144 percent
throat
to be operated the
blade
operation
These
from
rotor
shows
of stator
blade
determine
efficiency,
of stator
area
operation. area
to
turbine
a series
reduced
area throat
to vary
on
different
for
creased
order
speed
TURBINE_
Figure
1 0-15
for shows
13
the
combinations
envelopes
of the
1.00--
• 9O
.8o .2
¢_
_
WithConfigu design ration rotor With rotor extension -With cutback rotor
/,_/'" . 7O
I-,-
[
.6O
1
[
[
L
L
• 9C
.8_ t'oJ o
• 7{3
1 .2
.3
l
l
.4
.5
1
1
.6
.7
I
I
.g
.9
Specific speed, Ns, dirnensi_nless
FIGURE
t
t
I
I
20
30
40
.50
l
I
I
1
I
60 70 80 90 lO0 t3/4 3/4 t/2 Specific speed, Ns, _f )_lbm )/trnin)[sec )(Ibf 3/4)
10-15.--Experimental
variation of efficiency from ref. 8.)
with
I 1lO
specific
speed.
(Data
293
TURBINE
DE,SIGN
AND
APPLICATION
design-speed efficiency as well as the overall and-rotor ratio
combination
at
design
measured
for
design
ratio.
The
speed
and,
used
even off
turbine
might
stators.
In
the
from
overall
efficiencies
0.37
to
efficiencies
of about
of
be
considerably
of nearly
total
varying
over
0.80
(48
of about
0.4
to 0.5
pressure 0.90
to
were
103
(ft 3/4)
were obtained area was near the
0.90
were
(51
to 65
that
a
measured
(ft 3/4) (lbm31_)/
(lbf3/4)).
could
speeds)
by
Maximum efficiencies area to rotor throat
static range
with each rotor configuration, Specific speed for each stator-
simply
that
speeds
investigation
design
varied
a)(lbf3/4)). of stator throat
Maximum
(seC/2)
obtained curve.
Note
specific
specific
(min)
was
speed.
(lbm314)/(min)(seO when the ratio in the
curves envelope
parallel
though
the still
distribution
endwalls
volume
efficiency
of the
internal
efficiency.
in applications
the
total
flow
rate
remaining
stator
blade
specific
velocities
is
Further,
a radial
requiring
variable
varied
over
row
basic
(different
of
high
to advantage
with
particular
of applications
yield
investigation,
three,
8 showed
a variety
design,
be used
this
reference
for
by
0.90.
minimize
a factor
In addition, the
potential
for leakage. Effect Clearance avoid
of Blade-to-Shroud
between
contact
minimized
the
during to
blade
speed
avoid
loss
and
and
previously
discussed
figure 10-13, as determined
the
The
effects
rotor
must
transients, to
flow
fraction
Since
it
design
For
clearance
radial-inflow study
in figure exit
of the is the
flow
turbine
the
With
of passage
height),
294
percent
be
it must the
blades,
efficiency loss included in the losses
10-16,
which
at
the
rotor
efficiency
of reference
clearance.
flow
that
turbine
turning
clearance.
each
but
The losses
9. The shows
Increasing
were
results the
shown
in
clearance rotor-exit
increase
stator
can
equal
is fully that
be achieved inlet
there
was
and
exit
about
in clearance.
turned produces even
with
clearances a 1-percent
to
and
at
determined studies
of both
clearance
inlet
causes
a
does a comparable that determines
the the
inlet
of these
effects
exit
significantly greater loss in turbine efficiency than increase in inlet clearance. It is the exit clearance the
to
bypassing
unloading. one of the analysis.
be adequate
ratios.
in the and
shroud
clearance loss was based on an average from constant values of rotor-inlet and
on
presented
clearance
blade was
of blade-to-shroud
exit
experimentally are
due
specific-speed
clearance-to-diameter
the
the
thermal
of work
generation of turbulence, and due to blade-to-shroud clearance
Clearance
exit
blade
angle.
rotor
inlet
whirl,
a relatively (in loss
terms
large
inlet
of percent
in efficiency
for
RADIAL-INFLOW Exit clearance, percent of passageheight v 0.25 .92 o 3
4
"_E
0
TURBINE6
\ __
D
A
7
\ .E "-4
_"'-b_-. \
/
"<
1- Equal percent, exit and inlet clearance
1'-
-8
FIGURE
An
axial-flow turbine
of inlet
turbine would
passage
height)
rotor-exit
diameter
absolute area).
and This
energy level radial-inflow
the
have
a larger
than
would
a smaller
]
the
on
flow
relative
] 28
total
clearance
(percent
would
clearance height
(in order
of the
reasons,
along
of rotorThe
result
is largely
passage
(Data
as a radial-
turbine.
turbine
discussed, over a small
efficiency.
conditions
radial-inflow
required
be one
previously turbine
same
axial-flow
(since
may
and exit clearances from ref. 9.)
with
of the
clearance
diameter)
_ I
L.
4 8 12 16 20 24 Inlet clearance, percent of passageheight
10-16.--Effects
inflow exit
i 0
a function
to have with
larger
in a larger
the
for the efficiency axial-flow turbine
of
same
annulus
lower
kinetic-
advantage for the
of a same
application. BLADE The
curves
velocity
ratios
for
a particular
bine
size
part
of any
and
(figs.
to
10-11)
to specific
speed
turbine
problem.
shape,
as well
design
problem
in order
to determine
methods
and
used
10-8
the
computer
are
relating useful
They
can
as the
design the
best
stator
programs
turbine
geometry
in preliminary
involves
be used velocity
and
rotor
studies
to determine diagram.
examination
discussed
and
design
tur-
The
of internal blade
in chapter
flow
profiles. 5 (vol.
next The 2) are
for this purpose. Internal
Stator.--Stator forward. chords, large
DESIGN
blade
Typically, and
blade
parallel profiles
the
Flow
Analysis
aerodynamic
design
blades
relatively
endwalls. are easier
have
A long
chord
to machine
and
is
is usually because
relatively little
straight-
camber,
long
specified
because
the
number
small
295
TURBINE,
I_E_IGN
of blades lower serve
(long
cost.
AND
chord
Also,
long
as structural
associated
with
APPLICATION
means
large
chords
supports the
added
spacing
for
are desirable
a given
because
for the
shroud.
The
endwall
area
(over
solidity) the
stator
aerodynamic that
of
penalty short-chord
Pressure
.9--
.... Free-stream velocity
Suction
Pressure su rface
I
t
.2 .4 .6 .8 1.0 Meridional distance, dimensionless {b_
FIGURE
296
l()-17.--Stator
(a)
Blades
(b)
Surface
blades
and
passage.
velocities. with
surface-velocity
means blades
distributions.
blades)
is small
because
boundary-layer
of the high
parallel
flow
in reference
solutions.
Input
rate,
properties
fluid
complete
surface and
solidity,
and
number,
shown
in
figure
surfaces.
used
to determine If at the
angle if the
trailing
Rotor.--The than
that the
encountered The
for
screening
suitable contour,
This
onal
plane.
approach, uses
which
the
is shown
of velocities calculated
equation
the
10-18. in the
irrotational blades.
various
accelerations
11 is particularly
avoiding
severe
hub
and
blade
for radial-
with
several
integration
straight lines in the meridiof
these
meridional
Blade-surface
flow
and
quasisolution
velocities
of reference
blade-surface primarily
contour,
specifically
program
absolute These
geometries and
three-dimensionality
A complete
approximately
difficult gradients
distribution,
with
flow
provide
more pressure
method,
section
exit will
fixed arbitrarily located intersect all streamlines
is obtained.
on
blades
the
developed
design remain
Conversely,
of shroud
velocity-gradient along that
in figure
between
to evaluate
was
be
angle.
adverse
thickness
the on
the
free-stream
the
of
no are
may
curves
provide.
of reference
streamlines
based
distribution
smooth
and
the
combinations blade
edge
is appreciably of
a
has at
accomplish
flow
because
A meridional-plane
orthogonals then
blading
various
of directional derivatives (called quasi-orthogonals)
input
for
stator
trailing
can
edge,
the
program
of blades,
turbines,
trailing
and
profiles
velocity
for
and
continuously
the
blades
until
pressure
deceleration
can
value
because
computer
number
curvature. inflow
blading
design.
row
varying
velocities
accelerates near
the
by
of rotor
stator
(decelerations) of
the
the
the
small
magnitude
with
passage
surface
input
is specified
design of
a
and blade-
curvature
for
and
flow
blade
than
blade
entering
for
pressure
the
before
than
of
angles,
and
are made
obtained
flow
calculated
pressure-surface
the
the
and
method transonic
includes
acceleration
flow
because
and flow
The
trials
velocities
turning
cross
turning
edge,
edge,
more
curves
more
the
calculated
suction
specifies
outlet
and
blade
Except
whether
the
inlet
suction-and
10-17(b).
The
program
are
stator
subsonic
geometry.
stator
the
stream-function
distribution
which
leading
both
open
in
for
computer
for smooth
the
calculated
The
Successive
shows
pressure-surface
turning.
blade
and
turbine The
the
distributions
10-17(a)
radial-inflow
of
are examined
blade
prewhirl.
favorable
the resultant
satisfactory
conditions,
decelerations.
satisfactory velocity suction surfaces. Figure
and
be used
endwalls. for
specification of local
may
10 provides
information
velocities
rate
analysis
or near-parallel
described
a
TURBINE6
conditions.
A two-dimensional of the
reaction
RADIAL-INFLOW
a
are
11 with
linear
an
velocity
velocities
are
basis
of obtaining
on the
used
decelerations. 297
TURBINE,
DE:SIGN
AND
APPLICATION
1.8_ 1.6 Shroud contour
Quasi orthogonal oa
cfi [:Z
,,,,_
ela CE
1 .2
FIGURE
"In figure
I
1 l.O
10-18.--Meridional
Blade-surface ional-plane sections of
I
.4 .6 .8 Axial distance, dimensionless
velocity
section
distributions,
are
shown
the
blading, but as calculated by 10. The surface velocities
between
linear
method
does
velocity not
these regions. surface velocities 298
solutions variation reflect
the
radial-inflow
as calculated
turbine.
the
merid-
the hub, mean, and are shown in figure
shroud 10-19.
velocity
from
distributions
the stream-function calculated from
solution agree fairly well with over most of the blade. It can The
through
solution of reference 11, at a radial-inflow turbine rotor 10-20
difference
1
the
for
used blade
The stream-function in a more rigorous
at in
the the
unloading
leading
and
solution appreciable
trailing
meridional-plane that
same
method of reference meridional-plane
those of the stream-function be seen, however, that an
occurs
the
actually
method determines manner. However, the
edges. solution occurs
in
the blade meridional-
RADIAIrINFLOW
TURBINES
1.0 .8 _
_
Suction surface Free-stream velocity
.6 .4 .2 O--
.... _
I
t
I
I
.... 1
t
1
I
I
(al ,... 1.0
w
.8 o"
.6 .4
'_
•"_--
h
.2
-.2
F
-.4
I
1
I
I
fb) ].0
.6
.2_
....
____
0 -.2
-.4 0
.2
.4 .6 .8 l.O Meridional distance, dimensionless
1.2
t 1.4
(c)
(b)
Mean
FIGURE 10-19.--Rotor-blade
(a) Shroud section. (50-percent streamline) (c) Hub section, surface-velocity solution.
section.
distributions.from
merEdional-plane
plane program (ref. 11) is easier and quicker to use than the streamfunction program (ref. 10) and, thus, provides a better means for rapid screening of the many design variables. A lesser difference occurs in the intermediate portion of the blade passage. In the meridional299
TURBINE
I_EISIGN
AND
APPD£CATION
1.0 I
Suction
surface
.8 _Mean
.6 /
4
_
t- tee-stream
_--
""_/
velocity
.2
.... 1_1
0
t
1
J
__I__
I
_3b
1.0 .8
d 3
.6 .4
1
.2
% _2
0 q)J
C)
1.0 .8 .6 .4 .2 0
__----
1
()
.2
.4
.6
Meridional
L
._q
distance,
I _1
].0
1.2
1,4
dif]Te!_%lc,rqle%
_c_
(a) (b)
Mean
Shroud
(c) FZGURE
section.
(50-percent
10-20.--Rotor-blade
Hub
streamline)
section.
section.
surface-velocity
distributions
from
stream-function
solution.
plane
analysis,
the
flow
and the mean stream mean blade surface. blade
variations
blades
that
of blade Figures along
the
than
generally 300
and
velocities
flow path.
elsewhere the
from
then,
10-19
surface
Also,
in the flow
loading,
considered
and
defines
the
mean somewhat
10-20
illustrate
and
the
blade of the
is a region the
most
the
circumferentially
a mean
the loading,
is more
heavily
solidity
of high critical
stream
surface.
surface The
between
distribution
different.
blade lower
uniform,
blades follows the prescribed solution considers blade-to-
blade
is also
The
because
shroud
to be
surface between The stream-function
deviates
in the
is assumed
flow. region
hub-to-shroud
variations
as well
as the
variations
loaded
along
and
the
Therefore, and
shorter the
the
shroud
flow path. shroud
is examined
most
is
RADIAL-INFLOW
carefully
for
loading
favorable
near
the
siderably
higher
is nearly
axial.
previously 50 next
the
The
section.
percent
high
loading.
This
decrease
in blade
particular
rear
loading use
part
results
at
change
the
The
principally
indicated
inlet,
where
the
and/or by
large
using
the
the
Such
reduced
loading
of surface the must on
be made,
The
are
the
therefore,
this
effect
in the was
blades
splitters
shown
were
hub
almost
large
increase
study
the
in
trailing-edge
the
and
to
the
rotor surface
be
reduced
radial
10-3
part
and
used,
the
per
unit
losses surface area.
of
are com-
are
unit
use
turbine
area
of
A judgment
of splitter
blades
performance
The
splitter
calculated
will,
examined
designed
blades
with
then
were
in the upstream for both cases.
negative
indicated
half When
velocities
on
a reverse-flow
eddy
extending
50-percent
streamline,
what
been
meridional upstream
was
12. A turbine
tested.
the
loading data
showed the
when
of
of blade-shroud flow
conditions
velocity
and
favorable
12)
little
The
were
area.
had
result
clearance rotor margin
the
and
the
and
a
splitter
in
and
between
the
due
was
apparently
offset
the
previously
discussed
leading
tolerance
of speed
increase
to the
an insensitivity
rotor
reaction
a range
in efficiency
loss
indicate the of
over
removed
This near
taken
difference
cases.
splitters
surface
appreciable
(ref.
very
no-splitter the
to poor an
this
is excessive,
additional
the
at
blades
loss per
of reference and
blade
performance ratio
l l_e reduced
vide
great In
location.
Turbine
effect
the
pressure
boundary-layer
is now
on
removed,
of
the
increase
blade
75 percent.
it can
in figure splitter
reduced
blades
built
side
from
splitter
about
in the
removed, thereby doubling the blade loading of the rotor. Channel velocities were calculated
pressure
low
and
loading
blades
as to whether
of splitter
splitter
pressure
by the
be beneficial.
experimentally
the
r _)
in
section.
for the surface,
full
When
there
to offset
path hub
is highest
If
decreased
However,
blades
balance,
in
loading
suction the
blades.
results
area.
splitter
the
blades
splitter
_
be reduced a very
by
calculated
between
partial
called
flow
at the
to the (rVu
discussed
shows
long
inward.
on
are
flow
Blades
velocities
blades
primarily
could
decreased
blade
is radially
decelerations
the
to exit
the
momentum
surface
is con-
where
is due
inlet
The
radial,
exit,
which
hub
spacing
the
negative
partial
rotor.
monly
flow
by
inlet
near
inlet
blade
previously,
as indicated
the
rotor
angular
Splitter As
the
distributions.
is nearly
in
from
from
the
flow
of splitters, of the
spacing
turbine,
the near
loading
rapid
This
velocity
where
loading
high
through
section.
inlet,
than
discussed
in that
blade-surface
rotor
TURBINE6
edge.
by
of efficiency The
a radial-inflow toward
loading
low
turbine such
inlet pro-
conditions. 301
TURBINE,
I_E_IGN
AND
APPLICATION
OFF-DESIGN
PERFORMANCE
The performance characteristics different from those of axial-flow all
rotor
speeds,
pressure
ratio
inflow in
figure
The for
is only
rotation,
must
be
with with
variation
the
no flow
(see fig.
for turbine.
with The
Prediction studies
any
design to
in
modifications
design
transients
where
the
use
of
calculation studies.
system
methods In
the
is somewhat off-design
used
The
be
from the
4
E Z
.2
/
FIGURE
302
[
I
1,2
1.4
Inlet-total-
to e×it_staticq)res,_Jre
10-21.--Radial-inflow
1 1,6
turbine
flow
[
I
1.8
2.0
ralio characteristics.
select
matched in
these
that
used
geometry
o
1,O
help
not
Zero speeO
0
in
conditions to
.6
N
in
in system
approach
different
speed rapid
valuable
e_
¥
to that
more
operating
calculations,
.8
illustrated
are
may
geometry.
force.
be useful
be
components
variable
pressure
as blade-jet
can
also
across
similar
is slightly
various
can
ratio
ratio,
performance and
They
fluid
directed
centrifugal
is very
data
the
zero-flow
decrease
off-design
is built.
This speed
point
a radial-
on
pressure
turbine
efficiency
In
gradient
increasing
performance
start
hardware
study
off-design
for
Estimated
to examine
before or
techniques
situations.
small
turbine
as illustrated
force
blade-jet
ratio varies from the peak-efficiency the case of the radial-inflow turbine. many
is one.
10-21).
a radial-inflow
the
speed,
a pressure
of the
are slightly turbine at
when
centrifugal
is some
because
of efficiency
axial-flow
only
at zero
by
there
speed
section,
true
balanced
Therefore,
even
in this an
this
With
inward.
zero
to exit-static-pressure)
however,
increases
later
becomes
rotor
turbine
ratio
rate
10-21. the
radially
flow
(inlet-total-
turbine,
within the
the
of radial-inflow turbines turbines. In an axial-flow
is
RADIAL-INFLOW
fixed,
the
are blade rotor
working-fluid speed
depend
inlet
and pressure
conditions
on loss
ratio.
are fixed,
Losses
coefficients
selected
Joss and
the
A radial-inflow developed 13,
reference from
turbine
at
erence
the
and 14.
NASA the
mation
this
static in figure
10--22
for the agreement
10-22
variation
efficiencies
of mass plotted
10-23.
program
10-23
The
an accurate
flow
rate
against
calculated
is
and
presented obtained presenting
pressure
ratio
mass
pressure speed
efficiencies
and
flow
representation
with
in
by
The
blade-jet
in ref-
results
program
of speed
method
is described
illustrate
computer performance.
shows
and
between
calculation
computer
a range
stator
loss. Center
experimental
variables
the design operating flows are the rotor
performance
this
the
to force
Research and
of over
with
in figure
perimental
off-design Lewis
version
performance
comparing
kinetic-energy
associated
Figures
a modified
calculated
exit
and
calculated
calculated and experimental or design values at point. Additional losses considered for subsonic incidence
TURBINE6
esti-
of the
ratio. ratio
are generally
Total are within
exand
shown 1 per-
Percentof designspeed
Ii"
Experimental
120
70 90 100 110
Calculated -."-
¢-
_"-110
30 50
B
100 "- 110 90 Design 8O 1.4
1.5
I
I
I
I
I
I
1,6
1.7
1,8
1.9
2,0
2.1
Ratio of inlet total pressure to exit static pressure FIGURE
10-22.--Comparison
of calculated and design operation.
experimental
flow
rates
for
off-
303
TURBINE
cent
and
lations
DE'SIGN
AND
at most
2 percent
are
sufficiently
examination testing
of
the
accurate
to
of overall
system
various
components.
of the
1.00
APPLICATION
experimental provide
values. a
performance
valuable
prior
to fabrication
.__I__
the and
110
•80 --
90 _ _-. vu,, Percent of design speed
.70 --
5O
¢1)
"5
calcuin
--
• 90 --
c o_
The tool
Experimental
•60 --
70 90 100 ,_
• 50 --
llO
Calculated
Design ! •30
I
1
I
I
1
JJ
I
•90 --
,- 110
• 80 --
100 _'
.70 -o_
,60 -
•50 --
,40--
• 30 ,, .2
_ 30
I
I
I
.3
.4
.5
Desiqn
] ..... I .6
.7
I .8
J .9
Blade-jet speed ratio, U]"V i FIGURE
304
10-23.--Comparison
of calculated and design operation.
experimental
efficiencies
for
off-
RAD_AL-I"NF_A)W
TURBI_S
REFERENCES 1.
SAWYER,
JOHN W., ed.: Gas Publications, Inc., 1966.
2. 3.
SHEPHERD, D. G.: Principles RODOERS, C. : Efficiency and Paper 660754, SAE, 1966.
4.
LAGNEAU,
5.
bines. Int. Note 38, yon WOOD, HOMER J.: Current
J. P.:
Turbine
Engineering
Handbook.
Gas
Turbine
of Turbomachinery. Macmillan Co., 1956. Performance Characteristics of Radial Turbines.
Contribution
to the
Study
of Advanced
Karman Institute of Fluid Technology of Radial-Inflow
Small
Radial
Tur-
Mar. for
1970. Com-
Dynamics, Turbines
7.
pressible Fluids. J. Eng. Power, vol. 85, no. 1, Jan. 1963, pp. 72-83. HIETT, G. F. ; AND JOHNSON, I. H.: Experiments Concerning the Aerodynamic Performance of Inward Flow Radial Turbines. Paper 13 presented at the Thermodynamics and Fluid Mechanics Convention, Inst. Mech. Eng., London, Apr. 1964. ROHLIK, HAROLD E.: Analytical Determination of Radial Inflow Turbine
8.
KOFSKEY,
6.
Design
Geometry
for
MILTON
on Experimental D-6605, 1972.
G.;
9.
10.
SAMUEL M., JR.; AND of Varying the Blade-Shroud Turbine. NASA TN D-5513, KATSANIS, THEODORE: Fortran
HOLESKI,
FUTRAL,
KATSANIS,
THEODORE:
13.
14.
Use
in
the
SAMUEL M., JR.; Performance Evaluation Without Splitter Blades.
FUTRAL,
a
Surface
DONALD
in
CARROLL
to Estimate NASA TN
E.: Experimental Results 6.02-Inch Radial-Inflow
Calculating
Arbitrary Meridional
Transonic
WASSERBAUER,
CHARLES
of a 4.59-Inch Radial-Inflow NASA TN D-7015, 1970.
A.; AND FUTRAL, the Off-Design D-5059, 1969.
NASA
Velocities TN
D-5427,
Quasi-Orthogonals for Calculating Plane of a Turbomachine. NASA
FUTRAL, SAMUEL M., JR.; AND WASSERBAUER, Performance Prediction with Experimental Inflow Turbine. NASA TN D-2621, 1965. TODD,
a
TN D-4384, 1968. Effects of Specific Speed Turbine. NASA TN
of a Turbomachine.
of
AND
J.:
Radial-Inflow
Clearance 1970. Program for
Stream
NASA
WILLIAM
of
Flow Distribution TN D-2546, 1964. 12.
Efficiency.
NUSBAUM,
Performance
on a Blade-to-Blade 1969. 1 1.
Maximum AND
SAMUEL
Performance
CHARLES
Verification M.,
JR.:
of
A.: Experimental Turbine With and
A.: for
A Fortran Radial-Inflow
Off-Design a RadialIV
Program Turbines.
305
TURBINE
DESIGN
AND
APPLICATION
SYMBOLS Cp
D g H
specific
heat
diameter, conversion ideal
at constant
m; ft constant,
work,
J/kg;
pressure, 1; 32.17
or head,
based
J/(kg)
(lbm)
on inlet
(K) ; Btu/(lb)
(ft)/(lbf)
(see _)
and
total
exit
(°R)
pressures,
(ft) (lbf)/lbm
passage height, m; ft ideal work based on
inlet-total
J/kg; Btu/lb ideal work based
inlet-total
on
J
J/kg; Btu/lb conversion constant,
1 ; 778
K
conversion
2r
N
rotative
speed,
N,
specific
speed,
constant,
and
pressures,
exit-total
pressures,
(ft) (lb)/Btu
rad/rev;
rad/sec;
and
exit-static
60 sec/min
rev/min
dimensionless;
(ft a/4) (lbma/4)/(min)
(sec 1/_)
(lbP '4) total
number
P
absolute
Q
volume
r
radius,
T
absolute
U
blade
V
absolute
Yj
ideal
flow m;
relative
Ot
fluid
0
(full
partial)
rate,
mS/see;
ftS/sec
ft
speed, jet
plus
N/m 2 ; lb/ft _
temperature,
ratio, W
of blades
pressure,
K;
m/see;
ft/sec
velocity, speed,
m/see; based
m/see;
deg fluid relative
ft/sec on inlet-total-
m/see; flow flow
ft/sec
angle angle
measured
from
meridional
plane,
measured
from
meridional
plane,
deg Subscripts: flow
b'r
critical
h
hub
t
tip
U
0
tangential at stator
component inlet
1
at stator
exit
2
at rotor
condition
or rotor
exit
Superscripts" '
absolute
"
relative
306
total total
to exit-static-pressure
ft/sec
velocity, absolute
°R
state state
(sonic
inlet
velocity)
CHAPTER 11
Turbine Cooling, ByRaymondS.Colladay The inlet
trend
towards
temperatures
necessity
of cooling
requirements. foil,
In
while
bustor
the
frequently
term
of the
bled
the
airfoils
for
discrete
of
K
and
then
the
turbine
and
very
of air are
effective
]n
any
turbine on
the
configuration analysis prediction the
an
airfoil,
flow, profile
be
of the
requires the
cooling blade
which can
location
potential-flow
(pattern
factor)
the
hot
com-
temperatures
to
preserve
the
environment,
air
passages
main
gas
cycle
of the
stream
at
results
in
inevitably
overall cooling
one
vane,
meets flux
or
must
end
a given
up
thermodynamic
schemes
make
wall)
which
utilize
to the of
of
the
velocity of the
blade
the
gas
a complete
to
metal
arrive
into from
the
three hot
boundary-layer
transition
from
distribution, leaving
at
temperature
conceptually
understanding the
order
This
life air-
DESCRIPTION
design,
(or
broken heat
to meet The
internal
into
to the
to a stator
at peak
hostile
the
turbineled
required.
GENERAL
balance
in this
in the
walls
airfoil.
In
or vane.
and has
refers
row
through
blade
end
rotor
vane
is dumped
the
and
(2500 ° F).
is routed
Consequently,
a minimum
first
ratios
efficiency
"vane"
to the
the
components
around
across
vanes, term
refers
1644
turbine
cooling
efficiency.
cycle
and
the
enter
compressor
locations both
pressure
thrust blades,
"blade"
excess
integrity
compressor
chapter,
gases
in
from
turbine
this
discharge
losses,
higher to increase
the
energy a cooling
limit. parts:
gas
stream.
development laminar and
combustor
the
to
The
(1)
The This over
turbulent
temperature (or other
heat 307
TURBINE,
source).
(2)
provide tions.
I_E,SIGN
AND
APPI._CATION
A steady-state
a detailed And,
(3)
map the
blade, to
the
transient
of metal
prediction
for convection-cooling balance,
or
temperatures
entire
heat
transfer
through
coolant--must
To
be
the
treated
(see fig. 11-1).
The
heat
pressed
gas
adiabatic
would
reach
let
the
or recovery if there
adiabatic
were wall
the
flux
heat-transfer gas and the
is the
wall,
predic-
coolant
maintain
closure
flow on the
from
and
to
hot
convection
from
paths energy gas
to
blade
simultaneously.
product of a hot-gas-side difference between the as an effective
internal
process--convection blade
Let us for a moment oversimplify dimensional model of a turbine-blade surface
analysis
for blade-stress
of complex
calculations.
conduction
heat-conduction
problem wall on
to the
by considering a onethe suction or pressure
blade
can be expressed
as a
coefficient and the temperature wall. The gas temperature is ex-
temperature,
which
temperature
(the
no cooling).
for convection temperature
For
purposes
be
the
temperature
of this
total
gas
cooling the
surface
illustration, temperature.
Therefore, q=he(Tg'--Tw,
o)
(11-1)
where q
heat
flux,
hz
heat-transfer
W/m_;
Btu/(hr)(ft
coefficient
_) of hot
gas,
W/(m
2) (K);
(°R) Tg!
total temperature
T_.o
temperature
of hot gas, K; °R
of wall outer surface,K; °R
TW,
0
Tw, i
FIOURE 11-1.--Simplified
308
one-dimensional
model.
Btu/(hr)(ft
_)
TURBINE
The
heat
removed
from
the
wall,
expressed
in the
same
CIOOLING
manner,
q=h_(T_._--TJ)
is
(11-2)
where heat-transfer
he
coefficient
of coolant,
W/(m
_) (K);
Btu/(hr)(ft
2)
(OR) w,
temperature
i
T' C
of wall inner surface,K; °R
total temperature The
temperature
drop
of coolant, K; °R through k
q=-
the
wall
is given
dT k_ -dy=-[ (T_. ,--T_.
by (11-3)
,)
where kw
thermal
y
coordinate
1
wall
The
holds
is frequently For
number
a
Nu
only
done
he be
of wall, to wall
W/(m)(K);
surface,
Btu/(hr)(ft)(°R)
m; ft
m; ft
equality
coefficient plate.
normal
thickness,
second
As
conductivity
for constant
in a first-order
approximated
turbulent is given
by
thermal design,
conductivity. let
a correlation
boundary
layer,
the
for
the
heat-transfer
flow
fiat-plate
over
local
a fiat Nusselt
by
Nu,=
__gx__ 0.0296Re_"
(11-4)
8Prl/3
where distance Re, Pr The
along
Reynolds Prandtl Reynolds
number number number
surface
from
based
leading
on distance
is defined
edge
of flat
plate,
m;
ft
z
as
Re_ = pugx
(11-5)
la
where P
density,
_tg
component
_t
viscosity,
and
the
Prandtl
kg/ma;
lb/ft 3
of hot-gas
velocity
(N) (sec)/mS;
lb/(ft)
number
is defined
in x direction,
m/sec;
ft/sec
(sec) as (11-6)
where 309
TURBINE,
])E_IGN
AND
K
dimensional
C_,
specific
For
an
constant, heat
ideal
(11-4)
APPLICATION
gas,
at
1; 3600
constant
equation
sec/hr
pressure, can
(11-5)
J/(kg)(K);
be
Btu/(lb)(°R)
substituted
into
equation
to yield h =_
(0.0296)Pr
'/3 FPz'
" x
-/
k
Mx
_'g,
yW ,
#
I
T s
T--1
j
2\(v+l)/2('_-Dm
(11-7) where
p',
total pressure of hot ratio of specific heat constant volume
T
conversion
g R
constant
gas constant, Mach number
M On the
gas, N/m2; at constant
coolant
1 ; 32.17
J/(kg)
side,
lb/ft 2 pressure
(lbm)
(ft)/(lbf)
(K) ; (ft) (lbf)/(lbm)
a number
to specific
of cooling
heat
at
(sec 2)
(°R)
schemes
can
be used,
but
in
general, h_=CRe/,"Pr"=C(
w'_"
"]"Pr"
(11-8)
where C
constant
Re f
Reynolds
We
coolant
J
characteristic
dependent mass
turbulent
cooling
flow
Now, depicted the
hot
the
m2;
cooling,
m-----0.8
laminar
flow
pressure
are increased
and
the
wall
from
(11-1),
0.8 power
pressure
ratio),
for
convection
so the
cooling
otherwise
the
outer
is sharply
the outer
wall
11-2). gas
temperature
From
The wall
(i.e.,
At
the
same
(Tw._-Tc') flux
will increase.
to
the
(higher
heat
of
equations pressure
temperature.
T,_.o).
The
as
Tw.o is kept
through
difference
wall, Tg'
with
increases
reduced.
blade
temperature
temperature
air temperature temperature
the
increases
drop
efficient
be avoided.
temperature
increasing
temperature
wall
bleed
outer
Since
should
and
blade
raises
compressor
p_'
2 in fig.
with
n-----l3.
through
1 to state
flux
a fixed
profile
flux to the
it increases
T_._ for
sor
heat
and
decreases the
state
the
and
(m=0.5)
the
(going
temperature
m; ft
ft 2
when
heat
310
passage,
11-2,
and
removed,
area,
length___
lb/sec
in figure
increased
time,
kg/sec;
the
gas
geometry
characteristic
for coolant
flow
internal
on
consider
constant (11-7)
rate,
length
convection
is desired,
coolant-passage
based
coolant-passage For
on
number
compresavailable q must Therefore,
be
WPURBINE
COOLING
i
Tg
hg(T_ - Tw,o)
_ kw / _- (Tw,o - Tw, i I
1 / C
FIGURE 11-2.--Gas
h, must
be increased
case,
as seen
ture
and
and
an
from
infinite
by
figure
coolant
impossible
11-2,
coolant
reference
1 shows
required
for convection limit K
taining
in the
the or
we. The
inside
course,
through
limiting
wall
temperabe infinite,
this
condition
exceed
is
savings
cooling
only.
components
stream
Figure
cooled
cooling and
conditions
11-4
by
one
is about
while
the
use
cooling
illustrates
the
l l-4(a)
to (e)),
or more
of these
20
maincooling
cooling.
air with
air
about
temperatures,
convection (figs.
cooling
Figure
11-3
of transpiration as
compared
basic
to
methods
and it also cooling
for shows
methods
to (i)).
cooling
a protective,
and
to
11-3
increase.
convection
transpiration
in cooling
film
turbine of blades
or
in
temperature gas
the
a limit Figure
increase
blade-metal
film
on
pressure,
and temperature
these
operating
combined
l l-4(f)
as pressure of advanced
air-cooling examples
highly
restriction
is apparent.
turbine-inlet
To
the
and on its supply nonlinear
convection
gas
drop
he must
and
the
incorporate
potential
size cooling
hot-spot
reasonable
Film
the
Of
convection
application
pressure.
must
cooling
(figs.
flow
therefore,
passage
cooling
(2500 ° F)
atmospheres
shows
3, where
is required.
air available
of plain
designs
on temperature
coolant
are equal;
internal
of cooling
The
effect
the
is state
flow
capabilities
1644
pressure the wall.
increasing
temperature
of limited
quantity from
and
to achieve.
Because the
temperature
is an effective
by directing cool
film
way
cooling along
the
to protect
air into
the
surface.
The
the
surface
boundary effective
from
layer gas
the
hot
to provide temperature 311
TURBINE,
I_E_IGN
AND
APPLICATION
Convection cooling Film and convection
pressure, Pg, in, atm Turbine-inlet 3
4O
1400
1600
I
--
--
cooling Transpiration
cooling
lO
20
I
[
I
1800
2O00
22O0
Turbine inlet temperature,
2OOO
--
T_, in, K
I
I
t
25OO
3O0O
35OO
I
Turbine inlet temperature,
FIou]_.
l l-3.--Effect
of
Tg, in, oF
turbine-inlet flow
in equation (11-1) becomes flux to the blade is then
pressure
the
local
film
q=hg(T's_.,-where
T_,z_
frequently is the same The
tion
objectives 312
losses
which
designs
which
temperature
of film
pressures
transfer
total
yet
tend
and must
ensures
air into
minimizes
the
to reduce
temperatures. be integrated
blade
metal the
temperature
on
coolant
temperature,
and
the
T,,,,.) of the
assumed that the heat-transfer as in the non-film-coo|ed case.
injection
dynamic higher
is the
and
requirements.
(11-9) gas
film,
coefficient
boundary
layer
some
of the
The
loss in turbine
in K or °R. in
causes
this
turbine
efficiency.
aeroof using
and
an optimum consistent
It
equation
advantages
aerodynamic
to achieve temperatures
heat
heat-
configurawith
long-life
is
q_UR,BINE
Transpiration cooling
cooling
scheme
available,
currently
limit
heat-flux
conditions.
should and
because To
its
be small,
foreign
use
which
piration
cooling
A typical coverage
leads
figure l l-4(h), transpiration
the
however, less
cooling
from
is an cooling
attempt without
wall
is the operating
of blockage air
air
due
losses
into
the
blade
is shown
an array
of discrete
extreme the
be severe
boundary
other
trans-
schemes.
11-4(i).
Full-
as illustrated
in
to draw on some of the advantages paying the penalties mentioned.
of
Cooling air
Zn
holes,
layer.
that
cooling
in figure
pores
to oxidation can
be recognized
than
airwhich
under
cooling,
aerodynamic it must
efficient
drawbacks
transpiration
cooling
most
significant
of cooling
point,
transpiration-cooled film
has
to problems Also,
requires
blade designs
efficient
injection
latter
it
to advanced
contaminates. this
but
For
of normal
offset
of a porous
COOLING
_
Xn
(aJ
__
(bt
o
c:_
c>xE//Ej
(d)
J
JJ (e)
(a) (c)
Convection cooling. (b) Impingement cooling. Film cooling. (d) Full-coverage film cooling. (e) Transpiration cooling. FmuaE 11-4.--Methods for turbine blade cooling.
313
TURBINE
I_E,SIGN
AND
APPLICATION
Radial outward airflow into chamber1, Film cooled--_ \ Convection \_
i_f// 1/// /.////
L Impingement cooled
. /
f-Convection
inlet airflow
(fl
/_\lmpingement
cooled
Convection cooled
(g)
(hl
_Transpiration i,
cooled
//
Wire-form porous sheet
(il
(f)
Convection-, (g)
impingement-,
Convection(h)
Full-coverage (i)
HEAT
and
and
TRANSFER
film-cooled
FROM
General
314
equations.--The
boundary-layer
region
transfer very
blade
HOT
configuration.
configuration.
configuration. configuration.
GAS
TO
BLADE
Equations of heat
near
blade blade
Transpiration-cooled blade FIGURE I I-4.--Concluded.
Boundary-Layer
the
film-cooled
impingement-cooled
the
to the surface,
blade where
is confined large
velocity
to
'tURBINE
and
temperature
gradients
heat-transfer
are
process,
introduced
in chapter
Conservation
present.
the
Consequently,
following
6 (vol.
2), must
C(K)LING
to describe
boundary-layer
the
equations,
be solved:
of mass
o 0%(pu)
O (pv+
(11-10)
where time-average m/sec;
()' ()
value
velocity
component
in
y
direction,
ft/sec
fluctuating
component
time-averaged
Conservation
of
quantity
of momentum Ou . pu 6-_+(pv+p
_-7=7..,_ Ou v ) -_=--g
shear
N/m2;
dp -_+g
0 -_
(11-11)
r-t-gpB_
where T
local
B.
component
Conservation
stress, of body
lb/ft 2
force
in the
x direction,
N/kg;
lbf/lbm
of energy OH
.
_
OH
0 / 1
ur\
(11-12)
where H
total
J
conversion
Q
heat-generation
The u,
enthalpy,
dependent v, and
The for
the
H,
as denoted
solution
of
of heat
understanding tions but
bears has
turbulent for
eddy
little
persisted transport diffusivity
heat flux are contributions"
(ft)(lb)/Btu
W/m3;
in ch. and
and
6),
heat
layers.
H are with
flux
The
the
flow
overbar the
requires
the
resemblance of its and
momentum. sum
of
the
and molecular
our
of various such
structure
and
is Prandtl's the
to but
One
_,
expressions
hydrodynamic
use
to the
simplicity
(i.e.,
understood.
contribution
counterpart.
processes,
being
appropriate
through
because
as
the
values
is straightforward,
turbulent
heat
time-average
laminar
physical
of
(ft z)
requires
momentum
expressed
Btu/(see)
equations
of turbulent
in describing
which
1; 778
p, u, v, and
these
stress
boundary
diffusivity
Btu/lb
term,
variables
shear
thermal
J/kg;
constant,
limited assump-
assumption, of turbulence
success
in predicting
mixing-length
hypothesis
The laminar
shear and
stress
and
turbulent
315
TURBINE
DESIGN
AND
APPLICATION
p/
Ou
_--_..,\
(11-13)
and { aL_jj0/_
q=Ko[
_)
(11-14)
where yr,
laminar
c()mponent
ity), aL
laminar
,4
static
The
m2/sec;
diffusivity
(kinematic
viscos-
ft2/sec
component enthalpy,
turbulent
tional
of momentum of heat J/kg;
shear
stress
to tile respective
diffusivity,
m2/see
ft2/sec
Btu/lb u'v---; and
gradients
heat
flux _
in tile
mean
are flow
assumed
propor-
variable;
that
'tt'v' = -- vr _-ff
is,
(11-15)
and O,4 v-'_g_ ' = -- O_r _-_ where and
the subscript heat
T denotes
the
(11-16)
turbulent
(:omponent
of momentum
diffusivity.
Equations
(11-13)
and
(11-14)
can
p
then
0u
be written
p
as
0u
(t1-17)
and 0_'. _-_-- Koa
q=-Ko(aL+ar) The
preceding
boundary-layer
properties
and
flow
where
both
heat
cp is neglected
equation
,r
reduces
ar
and
there
mental
The
variable section.
properties
results
from
it
are These
an
is
are
taken
equations.--As
equation,
equations 316
final
under
then
integral
of
variation
generation,
assumed
must
laminar
in specitic the energy
approach
to
be
and
isothermal
to account will
of the expericondi-
for temperature-
considered
6 (vol.
2) with
solve
the
in term_
onset,
simultaneously.
'tssumed,
approximately
in chapter
convenient
at the
be solved
freq_)ently
corrected
corrections we saw
often
If the heat
arc
equations
usually
properties.
Integral tum
are
zero).
(inclusive
(6-42). properties
constant data
flows
is no intern,d
to equation
all boundary-layer
However, tions.
approach
(ll-lS)
as_u me t e lnperature-variable
turbulent
and
If temperature-variable analysis,
equations
compressible,
O/
in the
a later momen-
boundary-layer
of integral
parameters
TURBINE
such
as momentum
and
of discrete
velocity
thicknesses
derive
tion,
enthalpy
so the
displacement
profiles. their
Just
as the
meaning
from
thickness
eter for the integral defined as follows:
thicknesses
rather
displacement the
is a significant
energy
equation.
than
and
integral
O0_LING
in terms
momentum
momentum
equa-
boundary-layer
The
enthalpy
param-
thickness
/_= fo¢* pu( H-- H,)dY p,u,(H,,,.o--H,)
z_ is
Note the
that
the
subscript
subscript
g refers
e in chapter
to the
6. For
(11-19)
free-stream
low-velocity,
value
denoted
constant-property
A=fo_*u(T'--T',)dy u,(T_,.o--T,') The
enthalpy
ment
thickness
caused
The
by
integral
equation across
the
is a measure
boundary
energy
(11-3)
or
the boundary
equation
boundary
layers
the
resulting
integral
energy
with
that
if we make
pressure at
the
gradient, wall,
_, then equation
derived
either
the
equation
see for
and mass
by
transport
containing
details
decre-
integrating of
energy
the hydrodynamic
ref.
2).
In either
compressible
transfer
and
_ __d__ 1 du, q_ (H,_.°--Ht)dx 1 restrictive
at the
case,
flow
with
wall is
low-speed (11-21)
heat-transfer
flow
of constant (incompressible),
temperature reduces
coefficient
h,,x
difference
to its simplest
q c_,(T_,, o--T,')=
(11-21)
d (H'*' o--11,)]
assumptions
constant
Kpu, If a local
energy
-F PgU,c
= dh ____t_A [ (l_Mg)
flux
be
volume (for
properties
Kp,u,(H,.
zero
eonveeted
balancing
of a control
thermal
Note
of the
can by
and
q
(11-20)
layer.
directly
temperature-variable
by flow,
dA d--x
is defined
properties, no
mass
(T,,.o--Tz')
form, (11-22)
as
q h'.'=(T..,--T,')
(11-23)
h,., da Stz Kpu, c_,=d-x=
(11-24)
then,
317
TURBII_E
I_E@IGN
AND
APPLICATION
The group of variables on the left side is dimensionless the local Stanton number Sty, which is also equal to S
Notice
from
tions,
the
equations
integral
is called
Nu, t_--R_p r
(6-72)
and
momentum
and
(11-25)
(6-75)
equation
that
with
resulted
similar
assump-
in
CI'_--dO 2 dx For
compressible
thermal
flow,
energy
by
characterized as shown
by
wall
temperature uncooled
the
boundary
the
recovery
viscous 11-5.
within
in the
The
T,_,o, and
is dissipation
shear
an increase
in figure
were
there
is the
layer.
tz is the
flow,
the
dissipation by
turbulent
boundary
ing
the
that
temperature. sponsible allowing that
for
should
Prandtl
the
for energy
number
following
to
free-stream a high
kinetic
FZOUR_
318
l l-5.--Temperature
distribution
on
in
is related
to
°R.
For
laminar
Pr 11_, while the
adiabatic
of the
for
(re-
(mechanism
This
a high
temperature,
would
Prandtl and
suggest number
vice
versa.
Ii Tg,e
//
in
_
Iq " 0
a
a
wall
viscosity
diffusivity
layer).
energy,
r 2g-_j Cp---I
_
if it
Pr z_. It is not surpris-
ratio
thermal
u2
_'_
by
effect
wall
tg /
Thermal
an
boundary
adiabatic
reach heating
(11-27)
to equal
to the the
would
in K or
is the
is wall
or adiabatic
viscous energy
This
equation:
approximated
has
from
wall
into
the
ug2 2gJcp
number
dissipation)
to escape
a given lead
be
Tt.,,
of the
of kinetic
the
r is assumed
Prandtl
near
temperature,
can
layer,
The heat
static
factor
layer.
a measure
This
hot-gas
recovery
boundary
temperature
r defined
energy
temperature
gas temperature
Tg,=T,o.=t,+r ' ' where
of kinetic
the
static
effective
is, therefore,
factor
(11-26)
high-velocity
boundary
layer.
The
heat
(either
flux to the
effective
As we
have
terms ture
or static
seen,
The
gas problem
is to design wall
a cooling
temperature.
never
the
refined
The
effect
in
a
side
of the for
expression
gradient
wall
heat
flux
which
that
the
must
in
tempera-
blade
be
the
is to find
a
objective
a constant
surface
be
flux
always
hg.:`. The
varying
can
heat
temperature.
will yield
actual
layer
the
to the
the
(11-28)
gas-to-wall
coefficient
however,
boundary
to
outer-
temperature
surface
is
temperature
accounted
Boundary-Layer
blade
for
in
more
the In
surprisingly because the
blade
pertains,
flow,
proximation.
by
a
are
often
sense,
accurate the
to
for
the
fiat-
zero-pressure-
a first-order
correlation
close to those of more sophisticated Stanton number St is relatively
a cylinder
Though
only
enough
fiat-plate
correlation
around
region.
strict
to the solution the suction or
a fiat-plate
distribution
leading-edge in
results fact,
simplest approach coefficient on
coefficient
the
Equations
is approximated
a heat-transfer
crossflow
plate
the
approximation.--The that the heat-transfer
into
wall:
stages.
First-order is to assume faired
the case
heat-transfer
reality,
Solutions
pressure
and
in this adiabatic
configuration
thermal
design
the
In
constant. on
or the
for
gradient
to express
h,.,
temperature
in determining
expression
temperature
at the
it is convenient
temperature,
O00LING
OT, _ h -_ v=0---- g.:`(T,.e--T,_.o)
coefficient
gas
to the
temperature)
already
heat-transfer
The
gas
Ot Nlv=0 =-k_
of the
suitable
is proportional
q=--]¢'
difference.
effective
has
blade
TURBINE
yields
analyses, insensitive
apresults
primarily to pressure
gradient. For
laminar
dynamic energy
equation
similarity With
flow
over
boundary
the
wall
plate
both
be
solved
can
solution
a fiat
layers discussed
temperature
with
the
beginning
in
directly chapter
assumed h_.,=0.332
thermal at
by
the
and
means
6 for
the
leading
the
to be constant,
of
the
velocity the
hydro-
edge,
result
_ Re:,'12pr'z3
the
Blasius profile. is (11-29)
X
The
turbulent
counterpart
is given hz.,=0.0296_Re
The
local
For the
the
following
velocity
u_. x is used
heat-transfer correlation
in the
coefficient is frequently
by °" Spr'/a Reynolds he. ,, in
(11-30) number.
the
leading-edge
region,
assumed: 319
TURBINE
DE,SIGN
h,,'_=a
AND
APPLI_CATION
--80°_¢_80
E1" ]14k" _\ (p'u' _ _D'_'/_pro.,(l__)]
° (11-31)
where a
augmentation
D
diameter
The
factor of leading-edge
velocity
of gas
approaching
angular
distance
from
bracketed
diameter
term
D
(see
is the
fig.
11-6)
FIGURE
The
term
a vane from
highly
blade to
uniquely
leading
1.8,
have
leading-edge
factor
edge.
layer.
the
Kestin
with
yet,
turbulent (ref.
no general
Reynolds
number
the
boundary
ent,
it can
Reynolds stream 320
layer generally number
turbulence
studied
laminar
free
becomes
be assumed of 200 surface
of
amplification
velocities this
of
stream.
coefficient
approaching the
factor
of heat
heat
within
flow high
a fiat
plate
that
transition
000
to 500
roughness.
the
vortex thereby boundary
in detail,
transfer
with
will
to
occur
allow
with
zero will
000,
However,
a,
flux 'is flows.
stretches of flow,
phenomenon
turbulent
For
the
flow
stagnation region in the direction
sufficiently
to grow.
to adjust
magnitudes
of stagnation
is available. laminar to
and
a cylinder
favorable-pressure-gradient
fluctuating
3) has
range
deg
geometry.
used
This
large,
correlation
scale and intensity Transition from
ft/sec point,
for
mainstream
Various
used.
The highly accelerated flow at the filaments oriented with their axes increasing
m/sec;
stagnation coefficient
turbulent
been
associated
edge,
a cross-flowing,
11-6.--Blade
augmentation
or 1.2
leading
x/
for
the
ft
leading-edge
in
a is an
account
m;
heat-transfer
Ug,_ ==
to
circle,
but
turbulence when
instabilities pressure take
as
a Reynolds
in gradi-
place
depending
the
in the on
freehum-
TURBINE
ber
based
origin)
on
parameter. as the then
distance,
the
independent
state. comes
the
of x. A value
number
corresponding
for pipe
flow.
turbulence, An
For
from
the
blade
functional
layer
(see
momentum is given by
be derived (6-76))
2).
local
integrating
velocity
x is the
surface
meters
or feet.
The
tJo
distance
U,Sdx)
measured
momentum
of diameter
Fx
momentum assumptions
through
the
(6-76),
as to laminar velocity
+0,,_.
(11-32)
the
with
equaboundary
the
free-stream
stagnation
8,t_s at
D in a crossflow
variation
integral
\o. 5
2000
be assumed.
suitable
from
thickness
ReD=
free-stream
thickness
profile
given
Reynolds
high
can
of a variable
5 /
is, it is
to the
and
very
equation
as a function
where
the
making
that
is
layer never beof 0 but not with
plate
with
point
critical
momentum
from by
Upon
OL__O.67vO. Ug 3
of a cylinder
the
of the
thickness
layer;
of Ree.cr_t=200
for
can
form ref.
blade
0,
determining
in getting
000 for a flat
value
6 (eq.
for
a given
the boundary with the use
a local
thickness,
at
is a "universal"
a turbine
expression
chapter
boundary
developed
to Rex=300
a conservative
it is not
number
of the layer
(boundary-layer
momentum
number
history
over
the
Reynolds
accelerated flow, fact is consistent
flow
edge because
Reynolds
of Reoccur=360
approximate
on a turbine tion
in the
boundary
For a strongly turbulent. This
use
to use
critical
of the
how
leading
criterion,
convenient length
because
the
transition
is more
characteristic
immaterial
x, from
a practical
It
transition,
the
the
is not
O00LIN_
the an
point,
stagnation approach
in
point velocity
ug_ is 0.1D
(11-33)
°.'..- ?..o,5 ¥ Turbulent such as
or
that
transitional
flow,
(ouz0/u)_200.
The
2_
then,
value
exists
when
of x where
the
this
value
occurs
of 0 is
is denoted
T,cr_ t.
The
turbulent
the
equation
by
momentum
0T--
4.
L
This
assumes
Integral tum
and
accurate discussed. complexity
I1
method.--
The
solution the
than
the
penalty
of the
_g
transition
to obtain
approach The
,,,..
_/,g
an abrupt
energy
thickness
heat
_x-r-t,L._ti,----_e
in a similar
manner
]
(11-34)
from
laminar
to turbulent
of the
integral
equations
flux
to a blade
"fiat-plate
for more
computation.
is obtained
accuracy In many
of momen-
is a more
approximation" is, of course, cases,
the
more
flow.
refined
and
previously the
increased
sophisticated 321
TURBINE
DE,SIGN
methods
are not
method
accounts
and
effect
the
warranted
integral
Consider
in the
early
for free-stream
However,
the
specific
APPLLCATION
the
heat
more
temperature
assumptions
must
The
realistically,
on
still
integral
h=._ can
be made
also
in order
equations.
no
_p,u,cp
of design.
variation
surface
some
integral
and
stages
velocity
of a nonconstant
be included. to solve
AND
energy
mass
ax
equation
transfer
_ _
(eq.
across
u,
dx
(11-21))
the
wall
with
constant
boundary.
_- (T_.o--T,')
dx (T=.o--T,') (11-35)
Ordinarily,
the
solved
in
(1i-20).
to
Ambrok
equation
by
Stanton
making
that
the
length,
proposed independently
Stanton
and
that
fact
that
weak
this
can
approach of
show
If ] is independent give
For and
of pressure
us the
as a function
turbulent
(11-25)
flow
He of a
as the
character-
of pressure
gradient. ( 11-36
gradient,
functional
the
gradient.
Stx----f(Re_)
should
be
momentum
data
thickness
is independent
to
equation whereby
the
of pressure
be written
on enthalpy
function
an
have
5 in
experimental
function
number
based
first
thickness
solved
of the
number
would
enthalpy
however,
be
use
equation
the
to be a very
Reynolds
istic
4),
could
number
proposed
momentum
evaluate (ref.
(11-35)
equation
local
integral
order
then
the
flat-plate
solution
form.
over
a flat
plate,
combining
equations
(11-4)
yields St_=0.0296
Recalling
from
equation
Re-_ °2 Pr - 2/3
(11-24)
that
(11-37)
for a flat, plate dA
Stx=-_ the
local
thickness
Stanton by
number
combining
can
be
equations
St_ = (0.0296 Hence, (11-39) free-steam flows.) integrating
the for
function
f
from
turbulent velocity
Substituting
flow
expressed (11-37)
equation
enthalpy
so as to obtain
Pr-2/3) 1"25(0.8 Rea) - 0.2_
(11-39)
equation
(11-36)
by
(The
(11
of the
38)
and_
variation.
in terms and
is given
assumption, same
(11-39)
for
argument into
by any
holds
equation
equation arbitrary
for laminar (11-35)
and
yields Sty-
rT hg'_ l"kpe'_=C p
322
(11-38)
--0.0296
Pr-2/3(
T '
T
_o.z_/-o._
(11-40)
)
TURBINE
COOLING
where I =-: .f]_*.... p?I_(T_'--T.,o)' u
25 •
J,=,....
. ['0.SRe_(T/--
T_ o)71"25
(11-41) The
integration
is performed
enthalpy-thickness
Reynolds
laminar-boundary-layer
heat
to
a
equations
simultaneously
are
good
several
was
by
and
of
(eq.
kinetic
W.
In
addition
0z
to do
(o,y+ o
-_.v=p_
\0v/
Ov
of these
procedure
equations
of
for
(11-11)),
that
the and
of turbulent
with
ix given
There
One
(eq.
equation,
energy
of calculating
this.
to the
2.
boundary-layer
numerical
simultaneously
kinetic
°z/+lo,.,+¢,.'t
the
momentum
solved
the
approach.
the
conservation
also
of turbulent
available
(11-10)),
a fourth
all
critical
see reference
finite-(lifference uses
the
from
metho(1
solve
an
5).
(eq.
.._is
Conservation
l(ays (ref.
mass
(11-12)),
energy
a
details,
accurate
is to
programs
M.
P'ttankar
censervation energy
by
numerical
developed
Spalding
blade
with
ewduated
further
most
turbine
hg._,
being
For
solution.--The
flux
for
mnnber
equation.
IGnite-difference the
numerically
the
others.
by
az" -9
P(_+_)
0.v
(11-42) wheref/r The
is a turbulent
turbulent
kinetic
dissipation energy
is defined
.j//_
in
w'
the
is the
fluctuating
direction
All with lion wall
properties
are
no restrictive of surface
11
bound'n'v integration
Also,
in m/sec
plane.
mixing
the
locally
an(I
x-y
By length
effects
ix
the
l)rotile..Mass film
turbu-
boundary
made
assumptions
on
layer
the
varia-
transfer
cooling
the
calculated
of fi'ee-stream
through
local
or ft/sec,
including
are
at
the
also
handled
plots
showing
manner. example
the in
must
started
results
mmwrical
high-pressure
is given l,Jyer
the
m' velocity
cooling)
of
temperature,
a) (sec).
(1 1-43)
of velocity, the
or approximating
7 presents
tlcxihilitv
protile
layer. for.
temperature
(transpir'ttion
I;igtll'e the
to
evaluated
in a slraightforwar(I
Btu/(ft
as
component equation,
locally in the boundqry lence can be accounted
W/m s or
(u'2+v'2+w'2)
perpendicular
turbulent-kinetic-energy
in
1
2gd where
term,
figure
turbine l l-7(a).
be supplied (fig.
ll-7(b)),
from
apI)roa<:h wine. The
computer for The
initial
as a boundary but,
from
then
the
case
of
free-stream profiles
high-
velocity through
condition on,
a
the
to get, the
profiles
can
be 323
TURBINE
IYE,SIGN
AND
APPLICATION
2500-700 6O0
150(]
m
E
.
200 500 10C_ 0
_
(a)
I 0
I
I
.Ol
.02
I
I
O
.04
I
I
I
.03 .04 .05 Surfacedistance, x, m
I
I
[
I
.06
.07
[
.08 .12 .16 Surfacedistance, x.It
I
I
.20
.24
Total enthalpy (b)
I
(a) (b)
Initial
profiles
Free-stream reference FIGURE
for
reference enthalpy,
Surface
1.0447)<
I
106
J/(kg)(K)
turbine
} 1.O
boundary-layer
m/see
development
I .9
profile.
numerical 30.87
pressure
324
I
velocity
finite-difference velocity,
l l-7.--Boundary-layer
I
.2 .3 .4 .5 .6 .l .8 Dimensionless boundary-layer variable
.1
or
or
101.28
249.7 over
vane.
ft/sec;
program. free-stream
Btu/(lb)(°R). a
high-t_mperature,
high-
TURBINE
O00LIN(_
calculated through the boundary layer at discrete x locations. The boundary-layer thickness, momentum thickness, momentum-thickness Reynolds number, and heat-transfer coefficient are shown in figures 11-7(c) to 11-7(f), respectively. Notice that just upstream of the
• 16 --
.OO4
(c) ]
I
0
I
1
3.2_E
_, 2.4--
o8° I 60
E
(.3
¢-
E =
1.6
E
i°
*
>"
.8
b20
r-
I
[)--
20
(c) (d)
Pressure-side
Pressure-side
4O 60 Percentsurfacedistance boundary-layer
boundary-bayer FIGUaE
momentum
80
100
thickness. thickness.
11-7.--Continued.
325
TURBINE
DESIGN
20-percent
surface
thickness
(fig.
increase
rapidly
before
AND
APPLI.CATION
distance
11-7(c))
on
the
momentum
and
and
continuing
location
then
to
decrease
increase.
the
slightly
This
"blip"
vane,
the
boundary-layer
thickness over
(fig. a short
is caused
by
ll-7(d)) distance the
rapid
2400--
le)
I
1
I
I
I
80
1_
1600--
% m
t-
v
8.6_
_
_
7.0
ii '°
._
5.4
1000
8OO
"T"
3.8
-7-
600
2.2
4OO
I
0
(e)
Pressure-side (f)
20
momentum-thickness Pressure-side FIGURE
326
40 60 Perceni surface distance
heat-transfer 11-7.--Concluded.
Reynolds coefficient.
number.
_URBINE
O0_LIN_
48--
4[--
•8I
24--
.6
16-E E
E
>:.
>_
I .2bg
fl
(al
c
0l
(l--x=
g, o
48 -- E 8 r_
m
E o
E
e_ c21
32--
.8i--
24--
.6i--
16--
.2i--
8--
(b)
"--Total enthalpy
I
0--
_
I
I
I
.2 .4 .6 .8 Dimensionlessboundary-layer variable
(a)
Initial
profiles
ft/sec; Btu/(lb) (b)
1151.75 FIGURE
slot.
Free-stream
reference
reference
enthalpy,
velocity,
4.8189X108
609.6
m/sec
J/(kg)(K)
or
or
2000
1151.75
(°R).
Three m/sec
at
free-stream
1.0
slot-widths or
2004 Btu/(lb)
downstream
ft/sec;
free-stream
of
slot.
Free-stream
reference
enthalpy,
reference 4.8189X
velocity,
610.8
106 J/(kg)(K)
or
(°R).
11-8.--Boundary-layer
profiles
along
adiabatic
wall
with
film
cooling.
327
TURBINE
DE,SIGN
deceleration the
AND
and
APPL]:CATION
acceleration
of the
adverse-pressure-gradient
pressure
side.
about
the
Initial film
Transition
from
velocity the
have
to the
and
relations
involving
St, discussed
c_, which these
in earlier
all vary
transport
perature
with (and,
to results variations
temperature
are
Properties
or the are
analytical
corrected
common the ture
data
to account
use
for
the
In
the
latter
for
method,
(for
all transport
temperature-ratio
subscript
free-stream m=0.12. influence
CP static
For than
method
refers
to
coolant
the
local
side
are
heat-conduction up 328
into
a number
large
at
what
layer,
constantmethod)
Two
differences schemes
are
results;
the
in
namely,
reference-tempera-
are evaluated
at
the
flow, flow.
tg+0.22
(11-44)
(T_e'_"{ t_ "_" _] \T-_.J
constant
(11-45)
properties
For n=0.4
WITHIN
heat-transfer
Tg,_
assumes
temperature.
turbulent in laminar
CONDUCTION Once
and
tem-
Since
temperature
properties
Tw.o+0.28
Nu St N---_ce--Z-_c_=\ The
and
Usually,
property
gases)
of
coefficient)
constant.
variation.
Nu,
p, k, u, and
finite-difference
small
of constant
Pr,
dependence
boundary
in the
11-8 (b).
Re,
velocity
evaluated?
with
property
the
of
down-
: Tre.,':O.5
The
(except
method
temperature
the be
obtained
correction
temperature-ratio method.
reference
to
is
example
heat-transfer were
at
layer
gas properties in
occurs
in figure
temperature
the
across
properties solutions
experimental
in
the
widths
parameters
if properties
occur
the
an
3 slot
Fluid
a change
on
11-7(f).
shown
The
causes
layer
shapes
contain
therefore,
obtained
temperature property
sections,
edge
illustrating
dimensionless
temperature.
properties
profiles
compared
the
from
boundary
figure
About
Temperature-Dependent The
leading
of the
from
11-8(a).
changed
resulting
boundary
profiles
in figure
flow
of the
little
be seen
enthalpy
given
profiles
Very
as can
and
are
aft
a laminar
location.
state,
cooling
stream,
region
10-percent
in a transitional
mainstream
evaluated
laminar and
THE
coefficients
flow,
n=0.08
m:=0.6,
a
BLADE
WALL
on
the
at
much
hot-gas
the and
greater
side
and
known,
the
heat-flux
boundary
conditions
for
problem
are
available.
The
or vane
is broken
of finite
elements,
as shown,
blade for
example,
the
in figure
TURBINE
FIGURE
1 l-9.--Typical
node
breakdown
for
a turbine-blade
COOLING
conduction
analysis.
oj+4 _
I \ I \
_
f
-
iI
_
I
_
I
\
I
ii
J+
_
II
i
\\
I
II
il il ......
_11
oj+$ FIGURE
11-9,
and
a system equations then
be
computer. temperature thermal-stress Consider
l l-10.--Typical
an energy
boundary
balance
of algebraic equal solved Once
element
is written
finite-difference
to the
total
number
simultaneously such
a conduction
distribution calculations. a typical
by
throughout
boundary
element
for heat-conduction
for each
element.
equations,
with
of elements. means
of
analysis the
The the
equations
is available
figure
result
11-10.
is
number
high-speed,
is completed,
blade from
All a
analysis.
of must
digital a detailed for
use
in
Accounting 329
TURBINE
DESIGN
AND
for
all the
energy
and
those
transfer
adjacent
boundary,
APPLICATION
leads
between
to it
to the
+
(elements
following
)m+ k_Aj
dc Ac 1 (Tj--Tc'
the
T
(Tj--
• " • +_s
given
element
(the
jth element)
j-l-1
to j+5),
including
algebraic
equation
(see fig. 11-10).
_
j+l)
k_42 +--_--
5 (Tj--T_+5)"--
the
fluid
(Tj--Tj+2)"
pc_,Vj A(time)
(11-46)
(T']+I--TT')
where surface
A_
area
noted by
between
an explicit
the
may
equations
infinitesimal
transient
and
step
element
for every
the
n or n+
scheme
de-
or boundary
denoted
element
must
or steady-state,
If the
energy
l, depending
on whether
is used.
volume
transient
structured.
size,
heat-conduction
time
be either
are
or boundary
m 3 ; ft s
ra denotes
equation
calculation
element
i, m; ft
or implicit
A similar
and
i, m s ; ft _
ofj th element,
superscript
element
jth element
subscript
volume The
jth
by subscript
distance
44
between
element
balance
at
be written. depending
is allowed a point
The on how
to reduce
yields
the
to an familiar
equation 0T
(11-47)
Pcp0(time) where
x, y, and
z are
the coordinate
direction_.
COOLANT-SIDE There transfer
can by
impossible the local
problem
be many
CONVECTION
internal
flow
convection
to the
coolant,
to
each
convection-cooling
discuss
is to determine
coolant
the
temperature,
is not,
however,
can be very complex, must be known before An internal equations 330
flow network that
describe
as simple and the
is established, internal
used
for that
to promote
reason,
shown
he, and
the
equation
T'c)
(11-2) The
flow and coefficient and
be
Essentially,
coefficient,
previously
heat
it would
scheme•
as it sounds.
the internal heat-transfer
the
and
heat-transfer
T_, in the q----hc(T,_._--
This
geometries
coolant
path
pressure distribution can be determined.
conservation
pressure
flow
distribution
of momentum are
solved
_URBINE
to determine there
the
discussed the
flow
is interaction (convection
surface,
between
and
the
for
Fins
lators"
to keep
They
also help
most
effective
11-4(b)),
be
the by
highly
as seen
from
blade
and
the
convection
distance
Zn
D
is
boundary
11-4(b)
and
The
hole power
both
diameter,
m
on
functions
Reynolds
number.
thin.
One
of the
cooling
(fig.
cooling
the
inside
representative gives
\0.091
(11-48)
number wall,
based
on hole
diameter
m; ft
m; ft
the
of
and
as "turbu-
toward
(g). One
heat
(k_)
Nusselt dimension hole
deterscheme
layers
area.
impingement
irap-_-_lq_2ReDraprl/S
between
been
to act
surface
6 for impingement
impingement-cooling as characteristic
has
of
convection
air are directed
in figures
percentage
convection
passages
/,._ NUD,
the
coolant-side
mixed
of cooling
reference
After
cycle
he.
methods
jets
through
an iterative
particular
cooling
the
Since steps
conduction
of the
the
to the
increasing
small
of the blade,
correlation
flow
surface,
region
blade.
heat-transfer
to coolant),
to enhance
added
of the
three
be made.
for
used
parts
the
to
must
convection
where
gas
to determine
are
can
of
surface
a given
be used
methods
transfer.
hot from
correlations
must
Various
from
cooling
various
each
calculations
empirical
considered
between
convection
three
air available mined,
wall
split between
COOLIN_
Reynolds
the
number
and
impingement-hole
the
array
A least-squares-curve
coefficient geometry
fit of the
data
_1 and
are the
in reference
6
gives Xn
2
m----a_(-_)
Xn
+b,(,)+c,
(11-49)
and =expEa2 where holes
x,
in the
in table factor from
is the
11-I to
center-to-center
direction
for
rows
2
and
the
of ReD.
crossflow
in meters
coefficients
The
coefficient
caused
of impingement
(11-50)
x.
distance,
of flow,
as functions
account
multiple
xn
or feet,
a, b, and _o2 is an
by
the
accumulation
It
can
be expressed
jets.
between
c are given attenuation of fluid as
1 _o2 where
aa and
ba are
given
in
1 +a3_b_3
table
11-I,
(11-51) and
_b for
the
i th row
of 331
TURBINE
I_E,SIGN
TABLE
AND
APPLICATION
ll--I.--IMPINGEMENT-CooLING
Coefficient
CORRELATION
COEFFICIENTS
Reynolds number range, 3 000 to 30 000
Reynolds number range, 300 to 3 000
--O. 0025 • 0685 .5070
-- 0.0015 .0428 •5165
al
bl ¢1
a2
b2 c2 a3
b3
impingement
holes
is defined
0. 0126 --.5106 --.2057
0.0260 --. 8259 • 3985
0.4215 .580
0.4696 •965
as Go!
Zn
(11-52)
where Gcr
crossflow
Gh
impingement-hole
mass
FILM As
that
reduce
blade
in fig.
11-3).
cooling
metal
and
combined
and
cooling-air
are
in the
cooling
yields
film
convection
or
temperature coo]ing,
but
332
then
of combining
and region
cooling
cooling
the
cooling
air
same
film
only, all
lower alone.
film
cooling
only
the
wall
temperature
wall
also
that
the
same
and
of holes
full-coverage
much
only, hot-gas rate.
combined does
average
as for
either wall
convection
higher
or slots
surface
flow the
the
shown
cooling
than
Notice
to
convection
coolant
is about
arc
(as
same
hole,
temperature
of the protective film. film cooling from rows cooling
the
ap-
cooling
blade
film
for
percent
gradients
and
Here,
of the film injection
for
transpiration
film
11-11.
cooling,
it becomes by
both
in figure
convection
a significantly
increase,
conserve
for convection
(ft 2)
COOLING
be augmented
and
is shown
and
immediate
of the rapid decay First, localized cussed,
given
(ft 2)
(m 2) ; lb/(hr)
pressure
must
importance
conditions
Except
and
cooling
design
fihn
kg/(sec)
TRANSPIRATION
temperatures
The
(m 2) ; lb/(hr)
flux,
temperature
convection
in a given
temperatures
kg/(sec) mass
AND
turbine-inlet
parent
flux,
because
will
be dis-
discrete-hole
film
TURBINE
1800L-
_6
_
2600--v
/
:
I
J
_ ,A,'_|
f__'-
2200
COOLING
Hot9as
_3_1_"
Film coolingonly
_Convection _
coolingonly
Hotgas
1200 ---..Combinedfilm and convection cooling
_
_
1000
:_-
_ooI 0
FIGURE
l l-ll.--Effect
cooling.
To
i
of
l
combining coolant
successfully
film-cooled"
analysis
expression
temperature
I
I
the
becomes
and
on the
heat
the
film
must
be
preceding
flux
film
convection
model
coefficient
builds
for
film and flow rate.
analyze
heat-transfer
film-cooling ing
I
.2 .4 .6 .8 l.O Dimensionless distancedownstreamof slot
to
cooling.
cooling,
surface,
temperature
the
known.
"non-
Hence,
discussion.
the
Constant
In the the
follow-
effective
h,.x
is the
heat-transfer
Very
near
the
point
by
the
However,
the
effect
assumed
to be
adiabatic
wall
somewhat
from
of injection, injection
between
data
under
of an uncooled it and
correlated
the
hot
gas
in dimensionless
outer
T_, o is the wall).
The
injected film
out
film having
(see
fig.
form
by
effectiveness
and
wall
film
film
called (i.e.,
layer
film
it is the
of cool
decays
a'r
temperature
effectiveness
is
nl, z_:
T.,.--T_.,,, Tg..-- T', o temperature
the
it is obtained
conditions The
for this.
so _ is frequently
because
a buffer
11-12)). the
is altered
to account
is sometimes
cooling,
adiabatic
film
cooling,
coefficient
rapidly,
temperature
wall
_'"'"= where
heat-transfer
damped with
film
(11-54)
and _ is included
film
temperature
experimental
temperature
The
without
(he, x)I,,,_ hg, x the
itself,
is usually
unity.
(11-53)
coefficient
e --
gas
T),_m:
q=_hg._(T'.,,_=--Tw.o) where
the
(11-55) (coolant from
temperature
a value
of 1, at
at the 333
TURBINE
DE,SIGN
AND
APPIAI;C_TION Boundary
layer -7 /
Y I
_.,,_"_
_
I r_
T,
/
//
_'mm /
I
-J ....
'(
Coolant film
I Coolingair FIGURE
ll-12.--Experimental
determination
•+1:-___
+
deg
o++ 90 _'__----
.1 ---
+:_:
--%
08 --
._
.oz
I
10
_ I ,1,1,1
20
40
60
I
FIGURE
to zero,
of film
downstream.
of
(x--x_)
for
investigators.
is normalized
between
the is with
film
the
air and
the
respect
90 ° is perpendicular). increasing The film 334
As
injection following
cooling
to the
I 1000
hot-gas surface the
for
slots
s and
stream.
slots.
values
as determined the
The
(0 ° is parallel film
4000
experimental
downstream
width
, I
2000
xs#gs
gives
from
distance slot
seen,
(x
11-13
injection
The by
600
effectiveness
Figure
film
400
distance,
ll-13.--Film-cooling
effectiveness
number
angle
far
, 1,1,1,!
200
100
Dimensionless
slot,
temperature.
Injection angle,
1_ .8 _-"_
¥
of film
effectiveness
by
from
the
mass-flux indicated to the
a
slot
ratio
F
injection surface,
decreases
and with
angle. expressions
reasonably
well:
(from
ref.
7) correlate
turbine-blade
slot
TURBINE
Ik
_I'z'_=exp
for small
values
-0. 2
--2.9
k,p-_2]
of (z--z,),
OOOLIN(_ O.
_s
\p_u_s/
and
(11-57)
for large edge
values
of the
Values
slot,
of (z--x,),
where
z8 is the
location
in meters
or feet,
measured
from
for the coefficient
for a 30 ° injection angle. Film
effectiveness
distances ref.
from
the
8) for film
small
lateral
effectiveness
C and
angle,
and
as
cooling
a single
hole
downstream
and n----0.21
and
lateral
11-14
(from
of holes.
in this
distance,
case,
as previously
For film
shown
Dimensionless lateral distance from injection hole, hole diameters
o °
.40--
o
A
"_ E
30i_ xji_ ' "-_.,-'="_ " _ ."__
u:.
20--
,
.50
1.00
Plain s,,ymbolsdenote single hole at 35v injection angle Tailed symbolsdenote single row
_
I
FIGURE
a row
diameter
• 50 --
O
in figure
and from
1 hole
point.
for a 15 ° injection
downstream
is presented
up to about with
n are C----2.7
the
downstream
the stagnation
and n----0.155 of
hole
from
decreases
exponent 1.95
a function
injection
distances,
the
G=
of the
of holes
l
I
I
I
i
I
I
10 20 30 40 50 60 70 80 Dimensionless distance downstream from injection hole, hole diameters l l-14.--Film-cooling
effectiveness
as function
of
stream and lateral distances from injection holes. Mass-flux hole diameter, 1.18 cm or 0.464 in.; gas velocity, 30.5 Reynolds number, 0.22X 10 s.
dimensionless ratio, m/sec
] 9O
down-
0.5; injectionor 100 ft]sec;
335
TURBINE
DE,SIGN
for slots,
and
AND
the
APPI.,ICJ_TION
same
values
of holes. For larger lateral with downstream distance flow,
and
the
values
hole
because
that
_mm is not
of hot
of the
gases
surface.
for
the
row
interaction
unity
data
for single
of holes
are
are
larger
from
as for a row
jet
This
as
the
available
than
adjacent
hole.
film
holes
effectiveness initially increases of the spreading of the injected
injection
the
limited
obtained
of flows
at the
underneath
Very
are
distances, as a result
for
for the
holes.
is due jet
single
Notice
also
to entrainment
separates
from
a staggered
row
of film-
cooling holes. Frequently, the slot data are used for this case, an effective slot width s defined such that the total area of the equals
the
area
Figure single the
11-15
hole
of the
slot.
(from
ref.
at various
direction
of the
diameters,
methods
of cooling
boundary
through the this method extremely tion or
small and, contaminants
standpoint,
is one
mass
transfer
With
stream In
essentially order
cooling from
a large
surface.
This
In
amount
of heat
through
the
wall
maze of interconnected effectiveness. Convection
336
film yet
angle
of
persist
as
effective wall
into
convection
flow
still
is
as it passes in applying tend to be
v_o,v
obtain
cooling, cooling,
into
the
gas
some
of
the
full-coverage
the
is
a
of the
the
trans-
air
internal
flowing
flow
pas-
straight-through holes, or it may consist of a
a relatively
ability
in
pure
cooling
of the
term
issues
a continuous mass the other end. The
to tile
tortuosity
film
air holes
between
with essentially film cooling on
with
cooling
discrete
spectrum
convection
the
is a measure
the
efficient
air is injected
closely-spaced,
flow passages,
and
from
2 hole
to blockage due to oxidafrom an aerodynamic-loss
be constructed of simple, convection effectiveness,
effectiveness theory
the
lies in the
on
most
in
boundary.
the one end, and localized
depends
sages. The wall may with a low resultant
subject Also,
film
by
not
of the
in counter
problems
of small,
transferred
does
with
of transpiration
of cooling
piration cooling on flux over the surface,
exchanger
these
than
there are problems blades. The pores
are air. since
less
compound
film
a
angle
a very effective heat exchanger, wall from the hot gas stream
coolant
full-coverage
number type
the
the
cooling
However, to turbine
advantages
is used.
as the
to the
alleviate
characteristic
serves into
is paid,
normal
to
film
therefore, in the
a penalty
A
wall
to
small pores. of cooling
coverage.
of a porous
it combines
transferred
film spreads
with holes from
a 35 ° injection
but
cooling. The porous wall where the heat conducted continuously
the
film
of a film layer
For
coverage,
available.
layer,
spreading
stream,
local
lateral
cooling
the
of injection.
gas
very
more
Transpiration the
main
giving
injection gives far downstream.
8) shows
angles
the
borrowed of the
high
convection from
wall
heat-
(or blade
TURBINE
O00LING
Fi Im-cooling effectiveness, "r/film tO. 10
-2 -_
0--@
E
2
/
\
o r-
I
d
\
.25
--
1
'
6
_. 20
_. 15
1
I
I
I
(a)
r-
.g- -2 -.E
0 --
E
/
•30-I g
L. 25
X13
--
I
6
I
lO
L. 15
L.20
4 --
r.
I
I
I
I
tb) u_
_
-2 --
r.
25
"_,
E
_
2
\
4 -6
,-- .20
'--.30
0
I
1
I
I
I
I
5
10
15
20
25
30
Dimensionless distance downstream from injection hole, hole diameters (c} (a) Injection (b) Injection (c) Injection FIGURE
ll-15.--Lines
angle, angle, angle,
35°; lateral 90°; lateral 90°; lateral
injection, injection, injection,
of constant film-cooling injection. Mass-flux ratio,
acting as a heat exchanger) convection.
to transfer f
90 °. 35% 15 °.
effectiveness 0.5.
for
single-hole
heat to the cooling
air by
!
T c.o--T c.,.
(11-58)
Since an optimum design utilizes as much of the heat sink available in the cooling air as possible for convection cooling, ,7_o,, values approaching the limit of 1 are desirable. However, the convection 337
TURBINE I)E,SIGNAND effectiveness
is
available.
turbine
a
solid
ref.
perature
wall
by
matrix
The
resulting the
the
so does
the
cooling-air
pressure
model
in figure
metal
9).
through
wall,
limited
one-dimensional
blade
the
(see
usually
As Vco,v increases,
Consider on
APPLICATION
11-16. and
of
An
on the
wall,
Tw,
the
energy
and
local
be written
through
for
wall.
perforated
can
flow
coolant
the
or
balance
equations
pressure
through
porous
cooling-air
differential
supply
drop
local
the
wall
metal
tem-
temperature
in the
T'c, are d3Tw hv d2T,_ dy 3 _ Go% dy _
' hv dTw kw.e dy
0
(11-59)
and T'_=Tw
kw'ed_T'_ hr. dy 2
(11-60)
where effective
thermal
conductivity
Btu/(hr) (ft) (°R) internal volumetric
hv
of the
heat-transfer
porous
coefficient,
wall,
W/(m)(K)
;
W/(m
3) (K) ; Btu/
(hr) (ft 3) (°R) The
boundary
conditions
are e dTw @-_=o
(11-61)
_,)=kw
e dTw " dy _=o
(11-62)
11-16,
G_ is the
h_(Tw.,--T'e,_.)=kw, and
G_cp(T_ In this case, as seen of surface area. An the
overall
heat
energy
flux
from
ba]ance
to the
1,1-16.
wall
derivative, and matrix The side
and
They
heat
are
,--T"
figure
gives,
338
as a third
coolant both
temperature
nonlinear
heat-transfer
is somewhat
flux
boundary
to the
wall
can
profiles
with
which is a consequence heat transfer. flux
mass
o-- T_,_.)=Gc%_co._,(Tw,o--
per
condition
unit
for
opposite
of the
T:,_.) are
shown
signs
interaction
also be written
(11-63) in
figure
in
the
second
of
the
coolant
in terms
of a hot-gas-
coefficient: q=h,,_(
This
'
wall,
q=Gccp(T' Typical
'
different
from
Tz,e-the
Tw.o) heat
flux
(11-64) expression
with
local
TUR,BINE
OODLIN(_
Tw,o
1"1
C,O ]w,J
q
Gc
Tc, i
T__J
\
'\.,
_
ay--_t
c, in
hvA .,Xy(T w - Tc) '_
\
dl-w + dy d (k w, eA -_-y) ClTw_Ay kw,eA dy
\ \ '_
Typical element FmuRE
film
cooling
duced" than
in
11-16.--Porous-wall
that
the
heat-transfer the
acual
temperature
recovery
coefficient
film temperature
and
ht._ the
profile
gas
due
model.
temperature
to blowing
solid-blade
and are
used
heat-transfer
a "rerather
coefficient
hg,Z"
Consistent wall, not
with
which too
the
incidentally
large,
we can
local
one-dimensional
gives
good
results
model if the
pressure
of
the
blade
gradient
is
write F ht_ Stt_ _:;--_=eF/__
where
the
as shown mass
flux
correction in figure (surface
factor] 11-17
(from
averaged)
1J
is a function ref. to the
.
Str_
10), and hot-zas
F -(pu)_
(pu)
(11-65)
of convection Fis mass
the ratio
effectiveness of the
coolant
flux: (11-66)
339
TURBINE
I_E_IGN
AND
APPLICATION
Convection effectiveness, 11cony
1. E
0.9
o
J
f
J
J
f
• 7j
J
J
o
k_
.7
.6 0
1
2 Blowing
FIGURE
l l-17.--Correction
to
3
parameter,
equation
4
FtStcj '
(11-65)
for
wall
convection
effectiveness.
the
heat-transfer
SIMILARITY It
is
often
of
performance actual
of
engine
to evaluate size
turbine
the the
co_lditions.
conditions To
which are formance
and at
application.
a cooled test
answer
at
Generally,
hardware
actual
to
components
heat-transfer
to whether at
necessity
environment.
prototype
than
economic
this
other
tests
temperatures
practice
raises
design
similarly
question,
the
with
valid
various
actualpressures
question
as
specifications
under
actual
similarity
important in relating test performance of an actual-size film-convection-cooled
the
conducted
and a
meeting
behave
than
are
performance
gas
configuration will
conditions initial
aerodynamic lower This
blade
evaluate
engine
parameters
to engine turbine
perblade
are discussed. The number engine 340
Mach
number
distribution and
test
distribution around
conditions.
and the
vane
Similarity
momentum-thickness must in
be these
the two
Reynolds same
between
parameters
is
TUITBINE
essential
to
ensure
the
coefficient
and
adiabatic
transition
from
laminar
Let
superscript
same wall to
(t) refer
conditions.
To
tion
does
not
between
flow
must
be the
same
temperature
ensure
in both
F is an approximate
for the
variation
the
two
p;,.
and
local
point
superscript
Mach
/(RT')_,r(.
the
distribu-
equivalent
the
remain
local
_
(11-67)
eqs.
(2-128)
temperature
and
given
(2-129))
by
\(_+t)/2(_-t)
between
Reynolds
(t)
and
(e)
number
must
also
conditions,
o;,,.:.,
/z
#
(11-68)
momentum-thickness
unchanged
mass
,,
F-- _f_ _--_) Since
of
(e) refer
number
ry'
(from
with
/
same
Therefore,
'e' _(-R-_)g("
heat
the
heat-transfer
layer.
conditions,
correction
of specific
and
conditions
cases.
wy'--p'_
of
boundary
that the
w(.,,
where
distributions
turbulent
to test
to engine
change
relative
O00LIN_]
/(,r.);.,r,,, s
(p_),',-o;., .;') _"- ,".;',p';"
__
_,.,-1
(11-69)
\--_/z
If
the
engine
local and
(ou)J(Cu)z
,
(or density
conditions,
the
coolant
is
the to
0Jo_),
ratio
hardware
effectiveness
test ratio
hole-diameter size
film
and
to
coolant
hot-gas
the
OJD must
same
(11-69)
between
mass-flux ratio
ratio
(pu_)¢/(pu_)=
to film-ejection-
in both
cases.
Since
actual-
then
(_)(,, equation
hot-gas
momentum
--
and
to
unchanged
momentum-thickness be the
is presumed,
remain
--1
(11-70)
o;,,
becomes
_':' _","___,,"'-'"'e_I(_T_)',', r;" #g(t) w_" Equation with
the
pressure number Parametric for air.
(11-71) viscosity and and
,(,,p,(,,
shows
that
and
gives
temperature Mach curves
the the
which
number of
_/(R-_)z(,, gas
flow
(11-71)
(11-71)
rate
functional will
distributions
equation
Fg(,,--1
provide
must
vary
relation the
directly
between same
for test
and
engine
are
shown
in
gas
Reynolds conditions.
figure
11-18
341
TURBINE
I_E_IGN
AND
APPIAC_TION
4O
E
30
_ l-
20
eD
a_
i0
J
0 250
500
150
1000
1250
1500
1750
2000
2250
25OO
I
I
I
3000
3500
i
Temperature,Tq, K
FIGURE thickness
I
I
I
I
I
0
500
1000
1500
2000
ll-18.--Similarity Reynolds number
The
cooling-air
coolant-to-gas
curves of distributions
flow
rate
mass-flux
1
2500 , Temperature,lg, oF
constant around
and
ratio
Mach number a turbine vane
temperature
and
are
momentum
and momentumfor air properties.
then
ratio.
set
by
the
Requiring (11-72)
(7 ,J - L(--#u-),j implies
(11-73) Wg/
and
it is necessary
to ensure
equality
Neglecting in
the
that
of test
conduction
direction
T_,o is related
normal to the
and
engine
in the
plane
of the
to
wall,
the
supply
the
coolant
(He, o--He, (Hc.o--H_, where
the
(11-71)). hot-gas-side 342
viscosity
ratio
Satisfying heat-transfer
momentum
here
equations
ratios, wall
film
compared
ejection
temperature
since
(11-71)
coefficient
the to
that
by
mass (11-75)
distribution
to
temperature
,,)(t>_q(,) _,(_) ,n) (_) q(C) u_"
represents
pc.o=p_.
(11-75) flow
ratio
ensures around
the
(see
eq.
that
the
vane
will
TURBINE
have the same shape for both test transfer coefficient in dimensionless St(,'):St(, Since
the
Prandtl
similarity
number
conditions
number
ratio
equation
and engine conditions. Stanton number form
cannot
unity
The is
be
are
set
met,
depends
on
(11-76) independently
the
if all
departure
the
of the
Prandtl
the
Nusselt
coolant
side,
number
form
the
heat-transfer
is given
Stanton
number
ratio
where
m is the
power
tion. The viscosity coolant Reynolds factor
cannot
on the
in
dimensionless
/ _'* _'*' °_
Reynolds
factor number
be set
coefficient
(*'
number
in equation ratio. As
independently,
is small. In fact, if the viscosity t ct)¢.o could be approximated by
(11-77)
for coolant-side
(11-77) with the although
is the Prandtl
its
convec-
test-to-engine number, this
departure
from
over the full temperature a power law
then,
by equation
ratio
(based
perature)
(11-74),
tg(') to
(11-78)
test-to-engine
on
the
film-cooling
bole
would
be
1. The
coolant
simulated
same
conditions
through the
the
the
cooled
in the
engine,
which
remains
there
most
convenient
cooling
must
are
known,
same
test
wall
and
the
for
namely
the
for
same
the
two
during
wall
pressure as it does
temperature
conditions.
includes coolant
only
supply
Tf._.
Hence,
or some
similar
Strict
equality
actual
hardware,
scaled
properly
and
grouping
as a measure
pressure.
because
the
proportionately
of the
of these cooling
in _ for test since
the
because It
greater
temperature
of the
is easier
driving
three engine
lower
to cool
potential than
temperatures,
the for
at high
dimen-
is commonly
of a given is, however,
drop heat
those
(11-79)
performance
and
The
temperathe
T_.,--T_.o
used
temactual
conditions.
a test
engine
temperature
ture T_, _, and the effective gas temperature sionless wall temperature _, defined as
ejection
the
outer
and
number
number
ensure
normalized
between
Reynolds
Reynolds to
the
be some
dimensionless which
diameter
air passages
is to perform
invariant
temperatures
coolant
is important
internal
blade
unity
range
cc t_
If
in
by
Nuc (') =Nuc
drop
other
(11-76).
On
and
heat-
*) {'Pr(')Y/a
discussed
from
C_OLING
flux
blade
temperature
impossible
through
the
at reduced
at the
convection
blade
and
with is not
temperature
reduced
cooling
wall
design.
conditions, (T_._--T/)
pressure.
is How343
TURBINE
ever,
I)E,SIGN
for
and
AND
properly
APPI.JCATION
scaled
_(e) is well
within
test the
conditions, range
the
difference
of experimental
between
accuracy
_(t)
in most
cases. An
example
(11-71)
to
pressure,
of
(11-77) were
For
condition
a test
temperature
under directly
conveniently test conditions, in equation
rather using
_(_) is
than
high-temperature
344
than
and
equations
11-II
for
a high-
environment. a given the
what of the
air.
ratio
gas.
total
heat
radiation
and heat-flux
wall
be
conditions
Since
at the low-temperature be accounted for in the
fuel-air
Air
dimensionless it would
high-pressure with
solving
in
flux
the to a
and cannot
ll--II.--SIMILARITY
temperature
Takeoff
Gas total pressure, atm.
STATES
condition
Coolant
temperature
oF
_3500 200 400 600 800
1700 1811 1922 2033 2144
2600 2800 3000 3200 3400
905 1000 1200 1400 1600 1800 2000 2200 2400
condition.
' 33. 7 4.3 6.0 7.7 9.4 10. 3 11.1 12. 9 14.6 16.4 18. 2 19. 9 21.7 23. 5 25. 3 27. 1 28. 9 30. 9 32. 8
145 188 23O 273 294 315 357 399 442 485 528 571 613 656 699 743 786 828
is be
low-pressure ratio q(')/q(e)
(11-75).
_2200 367 478 589 700 758 811 922 1033 1144 1255 1367 1478 1589
' Reference
in table
air,
component
by film cooling
simulated it must
for
cooling
higher
be a significant
(a)
K
those
ambient
1 percent
affected
is given
by
gas-turbine-engine
TABLE
Gas total
generated
simultaneously
used
actual engine. Radiation can not
states
high-temperature
properties
blade
similarity
--199 --122 --45 31 70 107 182 259 335 413 490 568 644 721 799 878 955 1030
1.04 1.03 1.02 1.01 1.01 1.01 1.00 1.00 1.00 1.00 I. 00 1.00 1.00 1.00 1.00 1.00 1.00 1.00
TURBINE TABLE
11-II.--Concluded
(b) Cruise
Gas
total K
12200 367 478 589 700 799 811 922 1033 1144
condition
Coolant
' 3500 2O0 4OO 6OO 8OO 978 1000 1200 1400 1600 1800 2000 2200 2400 2600 28OO 3000 3200 3400
temperature _( t)/ _o(e)
!
oF
1255 1367 1478 1589 1700 1811 1922 2033 2144
I Reference
Gas total pressure, arm.
temperature
(X_LING
K
'13.8 1.7
°F
1801
1983
139 180 220 259 294 299 338 378
2.5 3.2 3.9 4.5 4.6 5.3 6.0 6.7 7.4 8.2 8.9 9.6 10.4 11.1 11.8 12.7 13.4
--209 -- 136 --64 7 70 78 148 220
417 458 498 539 579 619
!
660 702 743
,
729 804 878
782
!
948
1.00 1.00 1.00 1.00 1.00 1.00 1.00 1. O0 1. O0
ALBERT:
An Analysis
!
291 364 437 510 582 655
1.03 1.02 1.01 1.01 1.01 1.01 1.00 1.00 1.00
condition.
REFERENCES 1. EsQAB,
2. 3.
4.
5. 6.
JACK B.:
COLLADAY,
RAYMOND
S.;
KAUFMAN,
of the Capabilities and Limitations of Turbine Air Cooling Methods. NASA TN D-5992, 1970. KAYS, W. M.: Convective Heat and Mass Transfer. McGraw-Hill Book Co., Inc., 1966. KESTIN, J.: The Effect of Free-Stream Turbulence on Heat Transfer Rates. Advances in Heat Transfer. Vol. 3. T. F. Irvine, Jr.; and J.P. Hartnett, cds., Academic Press, 1966, pp. 1-32. AMBRpK, G. S. : Approximate Solution of Equations for the Thermal Boundary Layer With Variations in Boundary Layer Structure. Soviet Phys.-Tech. Phys., vol. 2, no. 9, 1957, pp. 1979-1986. SPALDING, D. B.; AND PATANKAR, S. V.: Heat and Mass Transfer in Boundary Layers. Chemical Rubber Co., 1968. KERCHFR, D. M.; AND TABAKOFF, W. : Heat Transfer by a Square Array of Round Effect
Air Jets of Spent
Impinging Perpendicular Air. J. Eng. Power, vol.
to a Flat Surface Including the 92, no. 1, Jan. 1970, pp. 73-82. 345
TURBINE 7.
DESIGN
AND
APPLICATION
ARTT, D. W.; BROWN, A.; AND MILLER, P. P.: An Experimental Investigation Into Film Cooling With Particular Application to Cooled Turbine Blades. Heat Transfer 1970. Vol. 2. Ulrich Grigull and Erich Hahne, eds.,
Elsevier Publ. Co., 1970, pp. FC1. 7.1-FC1. 7.10. 8. GOLDSTEIN, R. J.; ECKERT, E. R. G.; ERIKSEN, V. L.; AND RAMSEY, J. W.: Film Cooling Following Injection Through Inclined Circular Tubes. Rep. HTL-TR-91, Minnesota Univ. (NASA CR-72612), Nov. 1969. 9. COLLADAY, RAYMOND S. ; AND STEPKA, FRANCIS S. : Examination of Boundary Conditions for Heat Transfer Through a Porous Wall. NASA TN D-6405, 1971. 10. L'ECUYER, MEL R.; AND COLLADAY, RAYMOND S. : Influence of Porous-Wall Thermal Effectiveness on Turbulent-Boundary-Layer Heat Transfer. NASA
346
TN
D-6837,
1972.
TURBINE
CODLING
SYMBOLS A
surface
area
of one
coolant-passage
flow
augmentation
g
side
coefficients
in eqs.
body-force
component
bl, b2, b3 C
coefficients
in eqs.
cto,
aa
constants
coefficient.,
Cp
specific
heat
el,
coefficients diameter
d
dissipation term distance between
F
ratio
.[
hole,
correction
factor
mass
kg/(see)
g H
conversion
h
heat-transfer
hv
internal
/; I
static
and
J
conversion
K
dimensional
flux
thermal
hole,
or
film-
(m _) ; lb/(hr) 1 ; 32.17
J/kg;
mass
flux
(ft 2) (lbm)
(ft)/lbf)
(see 2)
Btu/lb W/(m
2) (K) ; Btu/(hr)
heat-transfer
(ft 2) (°R)
coefficien't,
W/(m3)(K);
fit s) (°R)
defined
turbulent
impingement
to hot-gas
coefficient,
enthalpy,
k
; Btu/(lb)(°R)
in eq. (11-65)
volumetric
,W
J/(kg)(K) (11-50)
circle,
used
constant,
Btu/(hr)
J/kg
; Btu/lb
by eq. (11-41) constant,
1 ; 778
constant, kinetic
energy, characteristic m; ft
exponents Nusselt
used number
in eqs.
exponents Prandtl
used number
in eqs.
pressure,
(2
heat-generation
q 1l
heat
flux,
gas
constant,
Re
Reynolds
r
recovery
factor,
St
Stanton
number
J/kg;
W/(m)
wall thickness, Xlach number
P
(ft) (lb)/Btu
1 ; 3600
(:onductivity,
eo()l'mt-passage M
pressure,
(11-49)
mass
enthalpy,
(11-57)
m ; ft
G
I
and
in eq. (11-42), W/m3 ; Btu/(ft 3) (see) volume elements (see fig. 11-10), m ; ft
of coolant flux,
lbf/lbm
(11-26)
of leading-edge
injection
term
(11-8)
N/kg;
to (11-51)
at constant
D
total
to (11-51)
in x direction,
eq.
m2; ft 2
(11-31)
(11-49)
in eqs.
element,
m2; ft z
eq. (11-49)
in eqs.
friction
C2
area,
factor,
B_
al,
of volume
N/me;
(11-8),
sec/hr Btu/lb (K) ; Btu/(hr) length,
(11-45),
m;
(ft) (°R) ft
and
(ll-4S)
(ll-S),
(11-45),
(11-56),
W/ma;
Btu/(sec)(ft
a)
and
(11-57)
lb/ft" term,
W/m_;
Btu/(hr)(fC)
J/(kg)
(K) ; (ft) (lbf)/(lbm)
(°R)
number eq.
(11-27)
347
TURBINE
DE,SIGN
AND
8
slot
T
temperature,
t
gas
%
component
APPLICATION
width,
m;
K;
static
°R
temperature, of
direction), volume V
ft K;
gas
m/sec; of gas
(y-direction), 'tO
component mass flow boundary
X
distance
Xn
center-to-center
Y
coordinate
Zn
distance
direction
along
surface
direction
normal
velocity
in
to
surface
ft/see
of gas velocity in direction perpendicular rate, kg/sec; lb/sec layer plane (x-y plane), m/sec; ft/sec surface
from
distance
direction
(z-
m3; ft 3
m/sec;
along
the
in
ft/sec
of jth element,
component
°R
velocity
of flow,
distance
edge,
m; ft
impingement
holes
in
m; ft
normal
between
leading between
to the
to surface,
impingement
m; ft
holes
and
blade
inner
wall,
m; ft heat F
diffusivity,
specific
heat
m2/sec; ratio
correction
ratio of specific heat constant volume ,h
enthalpy ratio
of heat
transfer
coefficient
coefficient
without
cooling
0
momentum
thickness,
tt
viscosity,
(N) (see)/m2;
l,t
momentum
T
(11-68) to specific
heat
at
with
film
cooling
to heat
film cooling
effectiveness m ; ft lb/(ft)
diffusivity
angular
distance
dimensionless coefficients
in eq.
defined
exponent
from wall
(sec)
(kinematic
density, kg/m3; lb/ft 3 local shear stress, N/mS;
term
eq. pressure
m; ft
7/
P
factor,
at constant
thickness,
transfer
ft2/sec
viscosity),
m2/sec;
stagnation
point,
ft2/,_ec
lb/ft _ leading-edge
deg
temperature (11-48)
by eq.
(11-52)
in eq. (11-78)
Subscripts: a
adiabatic
CP
constant
C
coolant
property
CFOSSflOW
COlbY
convection
crit
critical,
348
referring
to transition
from
laminar
to turbulent
flow
TURBINE
])
with
hole
e
effective
film
fihn
g
hot gas hole
h i
(li'uneter
at
free-stream
impingement inlet
J
jth clement laminar
J
with_._,
a,s characteristic
leading outer
edge
0
re]
reference
8
downstream
stag T
stagnation turbulent
t
transpiration wall
le
W X
local with
edge
length
value x as charttcteristic
with
A as characteristic
8
with
0 as characteristic
Sul)ersc,
condition
of slot
A
oO
dimension
inner
imp in L
as characteristic
C'(YOLING
apl)roaching
leading
length length length edge
ril)ts"
(e)
engine
(t)
test,
,
] total
condition ('mid ition stale
/ flu(:tuating
(referring component
to T anti (referring
p) to p, v,/,
u, and
w)
349
CHAPTER 12
Experimental Determination of Aerodynamic Performance ByEdward M.SzancaandHarold J. Schum The
preceding
theoretical deal
chapters
aspects
relating
of consideration
entire
etc.)
the
turbine
dynamic this
on
basis
it must
design
goals
have
turbine
shafting,
of mechanical
criteria.
be determined met.
design.
by
A great since,
hai'dware
bearings, Once
whether
Only
the
blading,
Associated
disks,
been
primarily
turbine
turbine.
(rotor
built,
and
with
toward
is the
and
concerned
directed
blading
the
been turbines
been
assembly
is designed
is designed
to
has
aerodynamically, the
have
casings
the
or not
testing
the
for
turbine the
aero-
turbine
can
be determined.
In
addition
of the The
to
separate stator
ments, obtained
overall
losses
loss
as
the
contributing
can
be
discussed easily
indirectly
chapter
direct
the
of a turbine,
to the
obtained
in
from
from
performance
overall
readily
from
7
2).
(vol.
stator
loss
loss
they
and
the
is often
experimental Rotor
measurements;
a breakdown
are
measure-
losses
cannot
usually
overall
desired.
be
obtained
performance
measurements. In
developing
determine ing.
the
which
The
obtain
the
test
of the
desired
the
test
stator
in which are
facility
performance
nature
manner
conditions
a
and parameters
facility,
and/or these
subject
program,
researcher
he is interested
the
instrumentation
overall
performance
parameters of this
the
vary
with
must
in evaluatnecessary
parameters, turbine
to and
operating
chapter. 351
PAGE _-_--'_
INTENTIONALLY 8LAtIK
TURBINE
DE,SIGN
AND
TEST The
manner
is discussed herein.
FACILITY
in which
parameters pressure
bine.
The
sures,
mass
flow
rate,
directly
in the
calculated
from
be
work,
and
ranges
performance
speed,
discussed overall efficiency.
of rotative inlet
speed
of the
tur-
exit
pres-
and
determine
facility.
computed
turbine
the to
test
not
for
rotative (needed
turbine
will
and
define
specific
define
torque,
measured
the
torque,
to fully
temperature
and to
determined
in order
inlet
2)
used
rate,
are usually
ratio
and
flow
is expressed
7 (vol.
generally
are mass
and
MEASUREMENTS
performance
in chapter
parameters
performance
AND
stator
in detail
The
These
APPLICATION
efficiency)
Specific
work
are is then
equation rN -dw
Ah'-_K
(12-1)
where ,_h'
turbine
K
conversion
specific
F
torque,
N
rotative
J
conversion
w
mass
N-m;
rate,
(2-49b)
depends
is based
on
the
1; 778 (ft) (lb)/Btu
ratio
based
on
of the
outlet
across
The on
outlet
outlet
the
outlet
static
velocity
accordingly,
of the
commonly
used
In the will
this types
of devices
be discussed.
discussed manometers automatic 352
section,
in
as are
the
generally
test
used
acquisition
this
chapter. gages data
and
all
efficiency
is
where
all
on
a pressure
component where
Rating
static
efficiency
of outlet
only
efficiency
efficiencies,
the
axial
is not which
as
were
1).
a representative
Data
axial
work,
where
meaningful is based
meaningful is useful.
Total
Static
is most
the
ideal
meaningful
efficiency
of only
total
2 (vol.
and electroaic
and
velocity
desired.
equation is always
define
recoverable.
Rating
is most
outlet
in chapter
or
by
pressure
to
is most
by the ideal temperature
shown
inlet
used
efficiency and
pressure
recovery
as
1). The
pressure
useful
is lost.
to the
component
2 (vol.
pressure is
velocity
turbine,
particular
velocity
and,
the
outlet
total
corresponding
discussed
lb/sec
of chapter
pressure.
however, of
(rad)(min)/(rev)(sec)
is obtained by dividing the actual work hh' work is a function of the turbine inlet total
or
total
Btu/lb
rev/min
kg/sec;
pressure
(2-48b) the
rad/sec;
constant,
flow
the
J/kg; 1; _/30
lb-ft
speed,
Efficiency work. Ideal and
work,
constant,
These with
to make
will
the
reduction
can
vary
from
computations with
be described,
required
and
slide-rule
acquisition
facility
on-line
and
measurements
systems visual to computer
will not
be
reading
of
completely process-
EXPERI1VIENTAL
DETERMINATION
OF
AERODYNAMIC
PERFORMANCE
ing. A general discussion of data measurement, acquisition, mission, and recording systems can be found in texts such erence 1. Description of Test Facility
transas ref-
A turbine test facility consists of the research turbine, a gas supply, an exhaust system, associated piping with control valves, a power absorber, and the instrumentation needed to make the desired measurements. A schematic diagram of a turbine test facility at the NASA Lewis Research Center is shown in figure 12-1. This facility, a photograph of which is shown in figure 12-2, is used to test single-stage or multistage turbines of about 76 centimeters (30 in.) in diameter. It is generally representative of most turbine test facilities and is used here as an example for this discussion. In such a facility, removal of the turbine rotor gives the room necessary to place survey instrumentation behind the stator and, thereby, transforms the rotating rig into a stator annular cascade. Most turbine component testing is conducted with temperature or slightly heated. This is commonly
Laboratory air system
Venturi
acilit
isolation
air at ambient called cold-air
Burst-disc
Vent to
safety valve -.
roof
Sonic valve
", ,_i_
•
Isolation,'
valve
valves
• _
/kl I-
Gas supply .f-
control
joint
-
_
valve -,
--I
Bypass control valve -,
Expansion Main exhaust
....
LBurner_j_,,,
L
-=
"-_ Main control.-
/
"@
valve
valve @ _,- Facility
isolation f
Laboratory system
FIGURE
12-1.--Flow
exhaust
schematic
of a turbine
test
facility.
353
TURBINE
DE,SIGN
AND
APPLICATION
ductim
:FIGURE
testing.
Performance
values
based
N/cm was
2 or
and
thereby are
to and
however, on
turbine
smaller
turbines,
turbine
inlet
the
for
the
larger
performance
where
can
to figure
12-1,
(40-psig)
air
be
the
model are
number, found
number
to
effects
to
the
this
effect be
the
applivelocity
same can
as those present
a
of Reynolds
negligible.
are more
obtain
in lower
actual
turbine
then,
This
conditions
results
in an
turbines,
varied
(10.133
test
values
numbers
was
Reynolds
pressure
Yet,
Mach
pressure
K or 518.7 ° R).
standard
Reynolds
of equivalent
turbine-inlet
be encountered
testing.
Only
of
(288.2
the
would
in terms
conditions
1). Using
near
than
facility.
reported
temperature
2 (vol.
turbine.
dissimilarity;
are
facilitates
similar
actual
number
and
levels
test
sea-level
temperature
power
diagrams of the
psia)
in chapter and
and
cation
standard
14.696
of pressure flow
parameters
on
discussed
12-2.--Turbine
proper
For
important, Reynolds
number. Referring N/cm2-gage venturi
meter
(16-in.)
air-supply
354
is located line
air for the system
of
in a straight for
the
purpose
turbine the
is supplied laboratory.
section
A
of the
of metering
by the
the
27.6-
ca}ibrated
40.6-centimeter air flow.
This
EX_PERIME,NTAL
DF_TERMINATION
piping
is sized
exceed
61 meters
(as was
device
in
the
per
all piping) second
pressure
required
for
and
a range
of
flows.
the
turbine
vides
a high
operator.
pressure
inlet-pressure protection turbine-inlet (30
main
pressure
in.)
of Hg
valve
permits
diverts
into
of lower
fine
be seen
valve
the
control
used
example
The
to
sonic
valve
and
turbine,
turbine-inlet (20-in.)
turbine
desired
was
76.2
bypass
pressure. lines
entry
line provide is the 50.8the
this (6-in.)
air
dual
(These
cm
control
The
to provide
plenum.
pro-
automatic
establish
15.2-centimeter
of the
to the
controllable
safety valve and vent Further downstream
control
devices
air-metering
valve
operation
(for
air
of
(12-in.)
50.8-centimeter
velocity
discussion
not
constant
of metering
section. is an isolation
burner
will
air-metering
a relatively
number
to facilitate
absolute).
two
velocities of the
A 30.5-centimeter
drop
(20-in.)
air
affords
the
A further
control. A burst-disc from excessive pressure.
centimeter
the
PERFORMANCE
Location
line
minimize
devices is presented in a subsequent Downstream of the venturi meter by
that
ft/sec).
supply
may
AERODYNAMIC
such
(200
high-pressure
upstream
OF
then entry
lines
can
in fig. 12-2.)
After
passing
altitude
exhaust
(48-in.)
main
control
control
valve.
These
pressure
through
the
system
ratio
turbine,
of the
and
valves
air
laboratory
valve
acrossthe
the
a
permit
discharged
through
(16-in.)
turbine
while
the
to
the
a 121.9-centimeter
40.6-centimeter the
turbine
is
operator
bypass
to vary
turbine-inlet
the
pressure
is
maintained constant by automatic control. This type of pressureratio control has been most successful with small turbines. With large
turbines,
large
pipe
volume
A burner its use inlet In
air.
controlling
422 In
avoid gas,
the
burner
inlet
at
to heat
lb/sec)
the
from
and
the
valve. because
the
turbine-
turbine can,
exit.
modified
high-pressure
is then
mixed
temperature air
of
control
burner of the
air
of bypassed capability
inlet
is to elevate
Some
heated
because
in phantom,
problems
is used.
(52
the
12-1)
jet-engine
turbine
second
and fig.
icing
the
amount
has per
(in
response
air is with
the
is maintained the
fuel
a maximum ambient
by
flow. air
This
flow
of
temperature
to
(300 ° F). general,
burners
a relatively
simple
combustion
the
turbine of the
and
desired the
burner
kilograms K
natural
The
a slower
commercial
burner
both
particular 23.6
so as to with
remaining
the
purpose
a single
to the
is
is shown
The
facility
for operation
heat,
between
temperature
bypassed
there
installation
is optional.
this
for
however,
in
products
the but
cost
and
performance are
and
generally complexity
using
gasoline,
inexpensive are
added
to the
calculations. used
only
of large
jet
fuel,
means air,
and
Electrical where
or natural
of heating
flow
these
the must
heaters rates
are
gas
provide
air. However, be accounted provide low,
because
clean of
installations. 355
TURBINE
DEISIGN
All turbines The
and
test
are against
following
be guarded
AND
A.PPLICATION
facilities
must
be designed
some
of the
potentially
by
constant
unsafe
Low
supply
(2)
Low
pressures
(3)
High
temperature
in bearings
(4)
High
temperature
of dynamometer
(5)
Low
(6)
High
temperature
(7)
High
(or low)
temperature
(8)
High
pressure
of turbine
inlet
(9)
High
pressure
of turbine
exit
(10)
Overspeed
(11) (12)
Reduced Excessive
(13)
Excessive
Interlocks starting. air
rotor
rotation
of turbine
line
and
some
of
water inlet
was
previously,
for
designed
velocity
with
gas
and
upstream
minimum
of
circumferential has
an
pressure
approximate
of 2 dynamic A short, inlet inlet low,
straight,
section
entering
and
measuring
turbine
356
the
from
two
in the
quickly
stops
and
facility.
sides;
A screen
to the
used
view also
to provide
further area,
in
this
of the shown.
test As
the
plenum
for minimum
is shown
ensure
turbine
effective
the
row
and
upstream
insertion
located
a symmetrical
blades.
giving
This
screen
a pressure
drop
of blades
for
temperature
(station of the
of probes
is provided
does
the
the
purpose
12-3)
blades. not
converging of installing
measurement
0 of fig. stator
between
devices.
is located
Since
the
significantly
The
about
1/_
inlet
velocity
disturb
the
is flow
blading. annular
blades 2,
to
passage
first
station
chords
A straight, station
valves
turbines
An enlarged indicated is
distortion.
distribution
annular
pressure
the
turbine
during
heads.
turbine-inlet blade
to the
as feasible
section
50 percent
the This
research
a plenum
pressure
shut
system.
turbine
alarm
Turbine
volume
a converging
prevent
audible
to rapidly
of the
air enters
casing
an
damage
of one
as much
gas
systems
only
heater
to prevent
the
exit
and
test facility is presented in figure 12-3. section with instrumentation stations stated
supply
gas
monitoring
a signal
diagram
water
gas rotor
Research A schematic
oil
gas
of turbine
the
as in the
in order
oil
]ubricating
outlet
provide
provide
must
rotor
orbit
as well
that
lubricating
dynamometer
of turbine
monitors
features.
conditions
dynamometer
of dynamometer
shaft
Others
inlet
and
of turbine
on
operation.
of turbine
clearance between rig vibration
Some
safety
monitoring:
(1)
pressure
with
fig.
to 12-3).
flow measure
passage the
Measurements
is also
provided
turbine-outlet are
made
downstream air about
state
of the
(measuring 2 blade-chord
EXPERIMENTAL
DETERMINATION
OF
AERODYNAMIC
PERFORMANCE
f Station 0
1
I
2 ]
1
I
I
Stator blade-t-
'LJ :" Rotor blade
Plenum
]'0 dynamometer
i
\
i! \
_
i
i_\ ¸,
\ CD-11683-11
[ -
FIGURe:
]engths bilize(1
downstream and uniform
Both
the
idealized The
inlet as
latter
tail
cone
axial
outlet
compared
to
a burner
vary.
diflicult,
passages
the aml
in the
rotor, sections an
for
the
this test
actual
positions
flow-property indicated
last
sake
reason
test
section.
air
is relatively
turbine
are
turbine the
row
weight
inlet,,
and
a
Flow-passage minimum
state
conditiolls
the
in varying
area use
somewhat
s_,ving,
measuring for the
sta-
installation.
turbine
of blades.
of engine
blading
passages
of straight,
is exannular
turbine. Measurements
measuring in
test
preceding
Flow-Property The
exit
jet-engine
the
is the
the
of the
Accurately
turbine
of turbine
where
immediately
Also,
after
diagram
following
is required.
aml
tremely
and
has
length
before
of the
immediately
diameters
flow
12-3.--Schematic
figure
stations 12-3.
There
are are
loe,_ted numerous
in
the types
uxia! and
357
TURBINE
DE_TGN
AND
APPLICATION x o • E_
Measuring stations
1
0
FIGURE 12-4.--Schematic
variations of probes will discuss primarily turbine and
to obtain
flow
outlet, In size
all
size
of the
turbine
mentation probes
can with
In small ated
respect the
could
limits
Static 12-4,
have
on the
90 ° apart,
are on
values
number
and each
four both
the
on the
taps
manifolded
are often
served
differ,
pressures. As part termine As
calculate 358
reading
of the the
explained the
blade
effect
on
being size
can the
inner
of research
stator a
station,
outer
associprocess,
consideration
as
walls.
This
section,
along
of the
blade taps
the
ob-
individual
desired
the
pro-
individual
and
information
Static-pressure
and
In order multiple
If the
it is often
this
figure
multiplicity
occurs
average
test,
distribution velocities.
reading.
true
in
opposed
distribution. and data,
circulation
be the
shown
diametrically
a single
flow
performance
subsequent surface
not
their
expansion This
of the
negligible.
with
turbine
The instru-
size
be considered
measured.
taps,
to provide may
relative
probes
of
data.
of probes.
and
some
and
irrespective overall
the
various
measuring
static-pressure in
passages of the
inlet
12-4.
same
the circumferential pressure amount of instrumentation however,
pressure
the
turbines,
static-pressure
vides a check to minimize pressures
an
the
pressure.--At there
flow
in figure
duplication
large
presence
temperature,
turbine
investigations,
require
whether For
at the
is shown
experimental
to the
turbines,
therefore,
usually
exit,
determines
of pressure,
located
of stages,
be afforded.
blockage
and,
turbine
instrumentation.
the desired measurements. We used in the example research
measurements
stator
or number
2
of turbine
instrumentation
as at the
general,
turbine
desired
The
as well
diagram
available to make the instruments
the
angle.
Temperature rake ]-otal-pressure probe Static-pressure tap Angle probe
to desurface.
is are
used installed
to
EXPERIMENTAL
along
the
tubes
that
the
hub,
mean,
can
blade,
problem.
0.0254
centimeter
so as not Inlet are
at the to
is shown pressure
The
unshielded
used
for
the
in.)
is limited
be
in
If
divided
among
being
discussed,
installing
the
taps
used
is
size
diameter.
A
however,
too
area
center
small
(a)
The and
are relatively
probe
shown
in
measurement.
station the
or more blades no
is desirable results
in a
which that
insensitive figure This
to yaw is
probe
has
I
Shielded
However, to define on
is about
0.48
for
is such some
also
40 ° .
commonly
an insensitivity
tb_ (b)
total-pressure pressure
to establish
used
such
Flow
probe.
turbine-inlet
sure.
and
One
in length,
12-5(b)
90 °
12-4)
passage.
shielding, twice
probes, fig.
20 ° .
circumferential
based
of
size
presented
(see
flow
FZ(_URE 12-5.--Total-pressure
value
the
approximately
a hole
ia_
testing
of
the
hole
small
number two
total-pressure of
12-5(a).
readings
about
shielded measuring
Flow I
The
the by
hole
in diameter
total-pressure for
thus,
inlet
in figure
(0.19
that
to yaw
in.) flow;
blade
turbine
pressure.--Four
all immersed
centimeter
can
pressure-tap the
blade.
time.
are located
probe
taps
PERFORMANCE
of the
one
research
(0.010
AERODYNAMIC
sections
large;
The
total
apart,
fairly
OF
in any
the
to disturb
response
tip
desired
For
and
major
long
the
blades.
hollow
and
be installed
then
adjacent are
D_TERMINATION
distribution
and
maintain
the
turbine-inlet
pressure
ratio
experimental
readings and a constant total-pressure
when
Unshielded
probe.
probes.
reporting
measurements
serve are
as a check used
on
during
turbine-inlet value
the
turbine total
that
turbine
performance
of mass
flow
rate,
is
presoften is a static 359
TURBINE
DESIGN
pressure, tion,
and
with
AND
total
the
APPLICATION
temperature
flow
angle
and
obtained
a assumed
by
the
to be zero
[-i,
at
following
equa-
turbine
inlet:
the
V &s%jT'"-"
(12-2)
where p'
total
P
static
pressure,
N/m2;
5'
ratio of specific heat constant volume
g
conversion
Aan
annulus
R
gas
T'
total
pressure,
lb/ft 2 at
constant, area,
1; 32.17
J/(kg)
K;
measured
This
calculated
more
rel)resentative
l)ressure
to
specific
(lbm)(ft)/(lbf)(sec
(K) ; (ft) (lbf)/(lbm)
temperature, angle
constant
heat
at
2)
m2; ft 2
constant,
flow
lb/ft 2
N/mg;
value
°R from
axial
direction,
of turbine-inlet of the
(°R)
true
(teg
total
aver'_ge
pressure
value
is thought
than
is the
to be
experimental
value. are
Inlet temperature.---Two located at the turbine
These
rakes,
contain
areas.
The
to determine and
the
Provisions
are
all the
the
wall
of
made
the
operation,
where
a constant
matic
regulation
Measurement for
the
was
latter
to the
to heat research
encountered
testing
conventional good shown 170.
360
length
accuracy This
inlet
modified
being
Reynolds
12-6(b) probe
shown
of
small
has gives
in
for
an
average
burner
in
Auto-
tmrl)ose. can did
example
present not
exist
herein,
but
as discussed
in ref-
wire must be exposed error negligible. The 12-6(a)
number.
The
has
a ratio
is inadequate
modified
length-to-diameter results.
this
number
turbines
figure
the
the
problem
12, whictl
excellent
12-6(a) area-mean
is maintained.
This as
radii
turbine.
as for with
of about a wire
the
a radial-inflow a.s well
Reynolds
used
12-6(a),
center
in figure
center,
is I)rovided effects.
shown
area
testing
at low
some
in figure
temI)erature
burner
to diameter
at low
in figure
duct
shown ,_1 the
the
of bare thermocouple make the conduction
thermocouple
wire
at
facilita.tes
turbine
in
rake
readings
conduction
erence 2. A large amount to the flow in order to exposed
outlet
of temperature
due large
particular
for individual The
a problem
to that situated
temperatures
readings.
fuel
siinilar
of thermocouples
annular
used
radius, of
are of a type
a number
of equal was
which
thermoeouple rakes, spaced 180 ° apart, inlet measuring station (see fig. 12-4).
of for
thermocouple ratio
of about
EXPERIMENTAL
DIhTERMINATION
OF
AERODYNAMIC
PERFORMANCE
! / /
/
/
I /
/
/
/
/ /
Thermocoul)le junction
Therrnocouplejunction
(a) (a)
Stator
stator probe
probe
is the
and with
blockage
testing,
the
rotor
Although
circumferential conventional
on the
rake
previously
testing,
is installed.
radial
associated
turbine
outlet
performance
survey outlet
type. 12-6.--Thermocouple
outlet.--During
at the stator
Conventional FIGURE
(b)
value
the
only
mentioned
wedge
probes,
measured,
also
For
a total-pressure to obtain
surveys, especially make
made
pressure.
and
it is desirable
type.
measurement static
is removed,
static-pressure being
(b) Modified configurations.
such
stator-
the
problems
the
effect
of
measurements
361
TURBINE
DE,SIGN
FIGURE
unreliable. from probe flow
angle.
The actuator driven
Note
angle
that
the
previously
the
test
hub
has
to be
sensing the
equipment
is shown of the
figure
does
probe regarding
not
This
have
the
same
that
wa_
average these
outer
in figure and
circumferential
effects
total-
12-7. the
and
probe,
(fig. 12-7) the
The
elements; inner
movement for
taps.
determined two
facility.
by interpolation
wall
survey
shown
Considerations
tip
test
in figure
at both
provides
in
is shown
for radial saddle
in this
and
previously probe
installed
are obtained
facility
measurements
provides shown
362
an
probe
pressures
at
in the
total-pressure
as the facility.
at
to obtain
probe
static
measured used
outer-wall
survey
required
values probe
is fixed
required
APPLICATION
12-7.--Total-pressure
The
the
pressure
AND
are walls.
12-8. the
movement. stem used
of stem
The
motorThe
configuration in the
blockage,
example sensing
•EXPERIMENTAL
DI_TERMINATION
OF
AERODYNAMIC
PERFORMANCE
r Outer wall saddleassembly
r Actuator t /
cm 0
5
LLLLU
C-06-2250 FIGURE 12-8.--Total-pressure
element diameter, edge are discussed Although example use
not
and measurement in reference 3. used
herein,
for
velocimeter,
velocity probes.
measurements
shown
in figure
12-9,
angle
the
of five
number
tional design,
with
the
side
tubes
and
are exposed
and the making connected
use
the
total
A laser allows
type
of sensing
pressure, Figure
general,
head
temperature,
are distributed circumferentially is located at the area center In
the
of flow-disturbing
probes probe areas.
exit.
4,
turbine
angle
probe center
direction.
into
12-4
turbine
shows
size
that at radius
influences
permissible.
of flow
self-balancing
with
discussion come
reference the
trailing
at the
annular
of probes
Measurement
without
as the
and
in
blade
recently
magnitude
of measuring
the
serving have
described
probes,
capable
are located
equal
facility
to be made
five of these combination measuring station 2. Each of one
as
outlet.--Combination
and flow
behind
techniques
velocity
such
equipment.
distance
particular
laser
measuring
Doppler
Turbine
in the
optical
directly
survey
tube
are symmetrically to a pressure
is accomplished
system.
The
used
to measure
located that
with ranges
by
probe
means
shown total
respect between
of a convenis of
pressure. to
the
the
a 3-tube The
center
total
two tube
pressure
static pressure. The openings in the side tubes are in planes an angle of 45 ° with the center tube. These side tubes are to
the
two
sides
of a diaphragm
in a balance
capsule.
A 363
TURBINE
I)E,SIGN
AND
FIGURE
differential so that tubes the
error
is generated
Exit
probe
not
used
are
than
does
true
if the
in flow
measurement occur
a self-balancing mined
is usually pressure 364
found
that more
the
integrated
range exit
operates
order
to
for
check of
for
and have
specific
use work
is especially
large
variations
conditions.
wouhl
gross
and
specific
This
position
the
are
efficiency,
of torque
values
temperature.
passage
reduce
measuremertts
of operating
in order
to
side
flow.
measurement
total
in the
of turbine
reliable
is in a fixed
diaphragm,
pressures
the
in
the
Even
to be work
with
surveyed
to be
deter-
of ideal
work,
accurately.
Exit is small,
into
values
of exit
probe,
results
probe
determirtation
the
by
the
total-pressure
probe over
when
and
been
temperature
is actuated
primary
provides
head.
A servo-system
the
to determine
(12-1)
angle
the
for the
It has
equation
capsule
unequal.
pointing
used
discrepancies.
and
are
by
total-temperature
they
of
signal
to zero
generally
sensing
in the
of the
but
12-9.--Combination-probe
transformer an
error
KPPLIGATI,0N
total
pressure,
which
determined use than
from
of equation does
direct
is used equation
(12-2)
yields
measurement.
for
the
(12-2). more
calculation When reliable
When
the
exit
values the
exit
flow
angle
of exit
total
flow
angle
is
EXPERIMENTAL
large,
the
become
DETERMINATION
radial
variations
large.
In
this
case,
(12-2),
ment
pressure
total
unless the
Flows on
pipe.
The
orifice
are
usually
the
pressure
primary
is not
placed
secondary pressure and on
in
the
recording
the All
the
computation
Each
of these
selection
obtained measure-
meters
rate
of flow:
fluid
meters
have
defluid
nozzle,
is flowing.
or The
or an intricate
has
certain
particular
advantages
meter
particular the
which in the
as a venturi,
the
of the
head
W=
be
meters,
manometer
of any
constraints
of the
passage
and
a constriction
such
which
and
variable
by
U-tube
the
exit
can
calculation
variable-head
caused
through
and
requirements of these
with
be a simple
device.
disadvantages,
values
between
is a restriction
pipe
may
in the
clear-cut.
differential
element
angle
PERFORMANCE
Measurement
measured element
and
integrated
choice
Mass-Flow
pend
AERODYNAMIC
in pressure
for use in equation of exit
OF
depends
application.
same
basic
equation
for
AtMCEY_/2gp.,(p.,--pt)
(12-3)
where A,
flow
area
of meter
throat,
m2; ft _
M
approach
velocity
C
discharge
coefficient
E
thermal
Y
compressibility
p_n
density
p_.
static
pressure
at meter
inlet,
Pt
static
pressure
at meter
throat,
The
approach
factor
expansion
factor factor
at meter
inlet,
velocity
kg/m3;
factor
lb/ft 3 N/m2;
lb/ft _
N/mS;
lb/ft 2
is 1
M:-
(12-4) 1
where The
D is diameter,
coefficient
actual
flow
rate
and
ferent
for
each
type
the
throat
area
C accounts
for
theoretical
of
dis<.harge coefficients bration of the meter expansion
4
in m or ft.
discharge
thermal
D,
meter.
flow
the
rate
Although
difference and
good
is significantly approximations
can be made from published data, should be made to assure accurate factor
is usually
E
accounts
determined
room temperature, which usually fluid flowing through the meter.
for
from is not
the
fact
measurements
equal
between
to the
a direct results.
that
the obtained
temperature
the diffor caliThe meter at of the
365
TURBINE
DESIGN
The
AND
APPLICATION
compressibility
factor
for nozzles
and
venturi
meters
is
(12-5) The
derivation
function
of equation
of pJpt_
and
concentric
orifices
determined
from
(12-5),
D#D,,
with
is presented
having the
along
the
empirical
equation
Ventur4, verging
which
section,
tubes
are
fuser the
tube.--Figure tube,
a cylindrical
usually
section object
12-10 consists
cast
usually
shows
important entrance
is made
section,
with
of accomplishing
and
machined
features
of
section, section.
The
The
of about
dif-
7 ° with energy venturipressure
in that
inlet
and
it is bulky,
reproducibility), a long,
the
difficult more
straight
throat.
run
The
venturi
to construct
expensive
than
tube
(particularly other
head
has
a
a con-
of kinetic
the
recovery
5:
(12-6)
surfaces.
angle
be
while minimizing friction loss. The total pressure loss from the tube inlet to exit is from 10 to 20 percent of the differential between
a maximum
most
can
reference
a diffuser
internal
an included
Y
')
the
have
of
from
of a cylindrical throat
and
Y as a
5. For
value
y --_ l -- [ O.41q- O.3 5 ( _-_--_/. )' ] ! P2_-_/
venturi
showing
in reference
(Ap/p_,)<0.3,
following
curves
disadvantages so as to provide
meters,
and
requires
of piping.
F low
"v_"
FIGURE
Flow
nozzle.--Figure
flow
nozzle.
tube
without
with
the
366
The the
venturi
flow
Pressure
12-10.--Venturi
12-11 nozzle
diffuser is thus
shows
tube.
the
approaches,
section. lost,
taps
and
The the
shape to some
high nozzle
pressure has
of a commonly extent, recovery a pressure
the
used venturi obtained
loss
of 30
EXPERIMENTAL
DETERMINATION
OF
Static-pressure
laps
AERODYNAMIC
PERFORMANCE
,
Flow Din
Dl
I
i
J
\,\
/// :: ii\\ FIGURE
percent
or more,
between approach 0.98.
the
depending
inlet
factor
M
and
on
the
and
streamlines
on the
0.65. vena
upstream
published cording
to make,
coefficients
ditions
is possible.
length
of the
The
cylindrical
of the flow
coefficient
the and
of the
differential
(7) for
be a high
upstream portion
(product
a nozzle
of
is about
is probably the most of the inward flow of
plate,
the
minimum
stream
orifice edge. This minimum area is it is at this area that the minimum
has a pressure flow coefficient
in most
pressure
coefficient
loss somewhat for an orifice
to the effective minimum at the orifice itself.
may
to specifications,
ratio, The
side
The orifice nozzle. The
This low value is due contracta rather than
It is possible
nozzle.
orifice (fig. 12-12) head meters. Because
area occurs downstream from known as the vena contracta, pressure is obtained. than that for a flow
area
throat.
discharge
Orifice.--The sharp-edged widely used of the various the
12-11.--Flow
machine
used.
edge must
being
shops,
an orifice
hole
is carefully
If the
degree
area
of reproducibility must not
be
exceed
sharp,
greater is about
with
which
made
ac-
of flow
con-
and
5 percent
at the
the of the
axial in367
TURBINE
DESIGN
AND
APPL]:CATION
L f low Din
Dt
- Static pressure FIGURE
side diameter more orifices the
orifice
12-12.--Sharp-edged
of the pipe. Because which will have the
is extensively
In
turbine-component by
the
performance. torque
dynamometer This
heat,
serves turbine,
converts useful
and
(1)
(3) electric methods other
than
brakes,
as the
generators
to
since
the
dynamometers
fluid
in figure
generally
used
in
speed
controller. in
as brakes;
dynamometer.--These is almost
12-13,
which
dynamometer
where
provides
(2) and
absorption into
this
for
section
types
the
include
electromagnetic
and
heat.
it generally
a load
(4) airbrakes.
force
turbine
the
turbine
discussed
dynamometer
absorption
is shown
be
the
surroundings,
brakes;
used
by
torque turbine
to determine Simply,
dynamometer turbine
of
in evaluating
used
supplied
to the
The
fluid-friction,
for measuring
Hydraulic
368
is dissipated
or
measurement
commonly
energy
dynamometers
hydraulic,
accurate consideration
dynamometers.
the
purpose.
this is used
Absorption
mos_
absorption
in turn,
no
an
is of prime
devices
cradled
it is possible to construct two or same coefficients when calibrated,
Measurement
tests,
turbine
The
are
orifice.
used. Torque
produced
taps
brakes; In
addition,
of torque
meters
are discussed. units always shows
are water. clearly
installations.
frequently A typical the The
cradle shaft
called
water
water
brake
mounting is
coupled
EXPERIMENTAL
DETERMINATION
OF
AE:RODYNAMIC
PERFORMANCE
Disk
Water in let -_ Shaft bearing\
/- Water in let
Packing gland ,, \
,/
/- Packing gland Shaft / /- bearing
Shaft
Pedestal bearing
FIGVRE
12-13.--Hydraulic
directly
to the
housing
through on the
it is free
housing
tends
housing
permits
absorbed
may periphery are
the or
is increased;
pacity
of the to
housing
rotate,
of Murray
the the
it.
A scale
of the
As
torque
rotates,
to
arm
moment,
fluid
bearings
shaft an
Co.)
to the
and
pedestal
the
attached
turning
Works
glands,
in the
limits.
Iron
developed
packing
is supported
_thin
with
disk
of the
closed
and
transmits
bearings,
determination
fed into
disk
The to
(Courtesy
and
the on
the
the
power
be computed.
valves
cient
disk.
and
shaft
to rotate
to the
the
turbine the
so that
Water
dynamometer.
test
friction
depth
Pedestal bearing
the
prevent
disk,
the
this
and
The the
where
inlet results
housing,
brake.
compartment
it forms
valves in greater
of water of
steam
by
a ring.
opened
frictional
the the
resistance
increased circulated at
centrifugal As
further,
a consequently
amount
formation
is thrown
any
force
discharge water
between
absorption should point,
ring ca-
be suffisince
such 369
TURBINE
DE,SIGN
action
would
level, the
the
AND
cause
cube
of the
outer
can
increase
Care
must
periphery.
supported
ends ing
on
device
vicinity
the
pedestal
the being
of these
the stator.
with and
desirable
the
the
erosion
Another that
12-14.
In
so that
stator
and
a small lines
teeth,
rotor.
this any
On
so that of force
can to
using
occur,
increase
more
the
torque
than
the
enter
stator
may
be
is
trans-
the scale. The in the starer in with
rotor
are
teeth
them
and
the
the
rotor
rotor
caused
is
by
energized
as the are
disk
device,
between
of force
and
dynamometer
when
air gap
near
friction,
way
is, by
arm and measured which is supported which,
disk
of magnitude.
of the
eddy-current
a coil,
lines
in the
increase
holes.
bearings
The
of the
tested,
particularly
as an order
staging;
of figure
to produce ends
a_
of torque
through-holes
as much
is by
carries
magnetizes of the
water almost
all fluid-friction
them
because
of the torque on the shaft,
starer
machined
constant varies
increase of
to further by
however,
views
The
through
tends
two
by means is mounted
face
This
with
dynamometer.--The
in the
current,
provided
capability
Eddy.current
(i.e.,
makes
a
brake
is typical
and
absorption
in the
power absorption one disk.
bearings.
versa)
are
be exercised,
particularly
With this
engines.
brakes power
of
characteristic
vice
nongoverned water
shown
This
and
dynamometers
for testing the
unloading.
capacity
speed.
of speed,
electrical-type
mitted rotor
momentary
power-absorbing
increase
Some
APPLICATION
with oppos-
principally
is moved
to sweep
direct
by
the
through
the
/- Stator I I
itator
Water passages-,,
c_:Q(_-_I /_
Shaft
___
bearing-_
_k_--7-_:_-i'---'_;
/'//
.... 'K
OCilile /-Shaft
', /
-:--_:
'
It
Scale
L ],
o
i
,lorquearmI
FIGURE
12-14.--Eddy-current
dynamometer. mometer
370
and
Engineering
(Courtesy Co.)
of
Mid-West
Dyna-
EXPERIMENTAL
iron
of the
stator force
stator.
causes sweeping
The
current
dynamometer
cylindrical stator
coolant
connected dc
cradled, to measure
provides
a compressor)
(a turbine
and
shaft,
windage
and
torque in order
the
added
they
power
can
absorber It
about
19 kW
mometer
that
is used (25
an
inlet
airbrake which
in
an it
direction
of
momentum power
from
straighteners
The
casing
and
axial
the
After and
the
of speed. For
is cradled loads.
diiection,
the
The
mover unit
acts
bearing, the
frictional
turbine
tests
smaller
turbines,
percentage
of
turbines, torque
the
these output,
the
air
and,
leaving
on the
thereby, the
iotor
arm
the
is attached
to
removes
entry of the stator, to the
research
passes
torque
wheel
tangential turbine
through
in an axial
to the
which
the
opposite
the
air
airbrake
is equal
bearings,
through
rotor the
of a throttle
to ensure axial inlet collector
absorbs
rotor,
from
air
The
than dyna-
a paddle
a direction
of
Research (less
consists
the
type
airbrake
either
is accelerated
rotor.
Lewis turbines
of the
with
in
is a
NASA
airbrake
a rotor
it
of
A torque
be
can
a pump
This the
the
small view
momentum
in
It
driving
dynamometer
testing
12-15.
is discharged
torque
rotor,
appreciable
at
for
a stator,
tangential
rotation
output.
Therefore,
developed
in figure
axial
or
as a generator.
during
blading, and flow straighteners of the air. After the air enters
gives
frame
to determine
turbine
torque.
A cross-sectional
collector,
or airfoil type and discharge
the
airbrake
was
hp)).
capability.
the
acts
be
be neglected.
extensively
is shown
valve,
often
in the
of a prime
unit
a
can
(testing
the larger jet-engine type when compared to the total
dynamometer.hThe
Center.
the
an
has
passages
it is driving,
measured
represent
type
with
output
as a function
turbine
wet-gap
absorption
researcher
removing
true
may
type, eddy-
a device
the
energy,
torque
a dry-gap
dynamometer.
When
the
torque
turbine power. For are generally small hence,
absorb
stator.
A wet-gap
from
power
the
The lines of this energy
dynamometers
to drive
to the the
losses
Airbrake
ment
by
flows
versatile
engine).
losses
to obtain
friction
and
as to
permits
measuring
is then
total losses
most
it is absorbing
capability
The
and
in the
motor-generator,
required
as well
when
driving
seal,
the
power
used.
required
electric
or a reciprocating
as a motor; The
dc
rotor.
Eddy-current
any
rotor. therein;
is called the
water
rotor
passages
12-14
contact
the
PERFORMANCE
the
with the currents
commonly
rotor.
to give
the
not
and
the
dynaraometer.--A
used
the
rotor,
in series
between
tluough
in figure does
is also
onto
stator or
water
iron-core directly
flowing
shown
the
attraction
water
dynamometer
AE.RODYNAMIC
to try to turn the stator induce
to cooling
because
OF
magnetic
the stator through
is dissipated The
DETERMINATION
direction.
on the
are
designed
the
casing
for for
flow
casing. radial
measure-
of torque. 371
TURBINE
DE,SIGN
AND
APPL£CATION
Thrust Journal Flow tubes_,,I\
il
-_-
t_-
I '
1,',-I Y_::_._:.._.__--"--?i
i_:_-
valve J
air
bearings
bearings-r-...
....
Throttle
air
_-z-.-X.Jl Inlet collector
1
,
-/
straighteners
x
i
[ \
/_
stator
i
_ _t_tteor r
I
. -J _.J
CD-10167-09 FIGURE
It
can
be noted
sections,
an
for
blade
each
extremely a stator
from
outer
momentum other
case,
the be
driving the
stator
opposite rotor used
capability,
Measurement Such
can
a scale
absorber forces relatively The readily and 372
torque acting
the
are
vertically,
for
regardless
small. of the
observable scales
may
not
of the
have
the
rotor. the
in this
aiIbrake
(It dynamometer,
This permits
losses. dynamometer by
Because
of
these
should
magnitude are
force
a spring-balance
displacements
of the that force
scale. the
scales
and
telescopes proper
rotor
For
turbine.
scale
(low-power
as the
the
the
impart
momentum Thus,
arm
of a spring-balance
can
design.
simply
torque
example,
to drive
frictional
the
row
of rotation
force.--The
because very
or
seal
most
the
blade
two
to measure For
tangential
type
of
valving
adapted
of rotation
case
and
used
arm
direction
power
consists
independent
pressures.
one
imparts
dynamometer be
horizontal,
available
turbine
inlet
where
direction
be obtained
disadvantages remotely
row
stator
is well
low
used same
as was of
can
system at
blade
of bearing
measurement
with
paddle-wheel
absorb
measurement
the
row,
in the to the
is of the to
that
blade
stator be
dynamometer.
12-15
outputs can
while
a direction
inner
This
turbine
tangential
can
an
configuration the
figure
and
row.
small
12-15.--Airbrake
indicate
does force
the have range.
power remain
involved.
reading been
is not used),
EXPERIMENTAL
DETERMINATION
Hydrostatic (e.g.,
air)
devices as the
of operation with
the
the
fluid,
produce
be
Most
particularly it
is
sorber,
signal
which
operates
strain
are
on
fine
the
through
the
The
the
a gas
principle
on the
greater
the
fluid.
fluid,
force
This
or force
has
on
fluid
required
to
slip rings, where this
type
occurrence with
system
torque
torquemeter
optical
projects each
separated
by
illuminated
reflecting
Experience
has
bearings surfaces.
kept
and/or
facilitate the
twist
intensity accurate
load.
the these
gearbox
strain-gage under
twist
highly
because
A higher
possibly and
be
difficult,
the
tile null-balance twist. that
reflecting
The
by successive onto
surfaces maintain usually
such The
must have
as
optical
accuracy. close
tends
to the to cloud
a laser
design
provide been
position
of the
to
systems
illumrepositions
are
torquemeters
photocells
Photocell
source,
end.
optical
unbalanced
oil mist
of
reflection
two
thereupon
readings.
the
at each
surfaces
light
and consists
polished and
equip-
measurements.
shaft.
produces
a
encountered
surfaces
of the shaft,
nearly
transmitted
life
the
condition.
bearings torque
Both
are
is
absorber.
basically
of a slit, on
Shaft
power
brush
A servomechanism
indicated
must be
twist
surface
is very
with
box.
gage
electronic
short
reflecting
the
image
gap.
to restore of shaft
fiat
surfaces
two photocells.
the photocells is a measure
torquemeter
and
shaft strain
Problems
torquemeter
measures
a hairline
on the
may
parallel unit
the
of the
optical
the
Readings
interfere
ab-
gear
and
to appropriate
that
the
torquemeter,
resistance
indicated.
for
wherein
of
wire
and
include
voltages
polished
torque
its
and
arise
strain-gage
applied. is
required
capability
A bonded
that
brushes,
as
of an intermediate
turbine
is
component
may
the
shaft
used. the
onto of
use
that be
strain
torquemeter.--An
A stationary
the
can signal
recording.
situation
than
a high-speed,
shaft
This
equipment
The
is higher
property
the
of induced
Optical a shaft
the
the
an
electronics,
voltmeter. data
calibrated provide
in turbomachinery
between
the
with devices
appropriate
a digital
cradle
can
of
equipped These
digital
principle
shaft,
function
ment,
with
necessitate
on
wire
unique
are
torque. on
problem,
proportional,
mounted
facilities
to
speed
this
torsional
load
measurement.
rotative would
optical
on
of the
which,
impractical
which
these
pressure
for automatic
circumvent
may
The
the
readings
torque
turbine
turbine
force.
or
is impressed
space.
torquemeter.--Sometimes,
conventional
This
mercury)
to measure
terms
test
suitable
testing,
ination
in
to measure
torque
Strain-gage
from
becomes
PERFORMANCE
(e.g.,
to be measured
cells
output direct
with
used
turbine
load
provide
The
a liquid
in a confined
calibrated
current
electrical
To
AERODYNAMIC
it.
strain-gage
the
been
force
held
greater
can
either
have
the
being
the
pressure
fluid
is that fluid
with
OF
beam,
of both for
operated
the
adequate in con373
TURBINE
DE,SIGN
junction
with
types
of
could
be
AND
APPL]_CATION
dynamometers,
torquemeters used
for
with that
turbine
good
are
One
of the
simplest
is that
of rotative
to give
a continuous
manent shaft
the
the
voltage
usually
and
accurate The
output
of the
in
tachometer
can
Adc
a rotating
generator
generator,
armature,
is to be measured.
indicator
measurements
electric
of speed.
and
of which
remote
most
speed.
field
speed
are
other
that
also
Measurement
indication
magnetic
There available
testing.
Rotative-Speed
testing
correlation.
commercially
is
Since
the
with
a per-
driven
by
the
field is constant,
is proportional
is a voltmeter
turbine be used
to its
graduated
to
speed.
read
The
rotative
speed. For
greater
revolution and
accuracy
counter
should
disengaging
called
in speed be used.
they
yield
are
an
with
is provided
a timer.
available.
average
a positively
A means
it simultaneously
chronotachometers,
because
measurements,
These
rotative
for engaging
Commercial
units
speed
driven
are
units,
advantageous
for a given
time
(usually
1 minute). The the
currently
most
accepted
use of an electromagnetic
larly
suited
sprocket An
for
with
electronic
given
time
Rotative supply
there to
number accurately
displays
speed
the
count
Since
faster.
accelerations
control
system.
It
provide
greater
accuracy
by one
performance
means
The
absorber
and
decelerations when
the
conditions contours
of speed
of equivalent inlet
conditions
of equivalent 374
maps. flow
and
of efficiency. conditions
the
a
air
power
pressure
to correct
are tends
for this,
the
and
accuracy
a steady
of
air supply
data.
and
of turbines Such
flow,
so that are
the and
discussed
usually
presented
map
as functions
of the
ratio. work,
are
a performance
work
pressure
The
of temperature conditions
for
PERFORMANCE
characteristics turbine
therefore,
to have
taking
shaft.
when
in supply within
a
speed.
and,
tends
ideal
turbine
tests
rate
method,
(or impulses)
turbine
an increase
is, therefore,
of performance
figure,
flow
this
to the
teeth
is through
It is particu-
as rotative
during
mass
TURBINE The
the
directly
to pressure,
For
is secured
counts
speed
counter.
machines.
somewhat
varies.
turbine
result
pulse
of teeth
the
varies
proportional
to drive the
a given
pressure
directly
of measuring
high-rotative-speed
pickup and
method or electronic
Also and
map
shown
speed can
pressure.
on
are
The
concept 2 (vol.
on
operating
the
shown
be readily
in chapter
shows, map
are
in terms
used and 1).
for
any
nature
EXPERIMENTAL
In
brief
DETERMINATION
review,
the
OF
equivalent
AERODYNAMIC
conditions
w.q=w
PERFORMANCE
are
--_ e
(12-7)
_h'
ah;q=
0
(12-8)
and N
Ne,= where rection
the subscript eq refers factors are defined as
to
o=(
(12-9)
the
equivalent
condition.
The
V_,,o ) _ \Vc_. ,,a/
cor-
(12-10)
_=p,'0 Ps,a
(12-11)
and ( e--%'a
2
"_%,_/(,.ta-_)
\_-_-t_+ 1/
(12-12)
( 2 y,(,-,, where
the
square
of the
critical
velocity
V_r=
The
subscript
pressure
An
specific
flow
and
the out
follow,
there
variations
may
ratio Also,
in this
performance
a
great
the speed.
or no
speed.
deal a better
if some as functions
curves
type
to be
of
are
included
of pressure
be
of the
performance ratio in the
mass
flow
to
rate
With
ratio
(total
presented
on
the
for completeness. can
understanding
presented
are
Equiva-
discussion
pressure
speed
information
of the
mass
of constant
or
conveniently
in the
in the
K
equivalent
product
shown
of
(1.4).
12-16.
of the
This be
constant
ratio
in figure
variation
Lines and
conditions (288.2
heat
product
as will
air
temperature specific
is presented
rotative
independently of this
and
of efficiency
map,
obtained
psia),
(29.0),
because,
case)
sea-level
14.696
against
be little
contours
Although be
data
(12-13)
standard
map
is plotted
in rotative
pressure
_ or
equivalent the
2----Z-_ gRT' 3,-t-1
the
weight
performance work
spreads
to
N/cm
molecular
example
lent
can
refers
(10.133
518.7 ° R),
map.
std
Vc, is
obtained turbine
parameters for
a range
following
from
the
performance are
plotted
of speed. sections
The
are not 375
TURBINE
DESIGN
AND
APPLICATION
Percent of design equivalent speed, N/%/B Ratio of inlet-total to exit-total pressure, pb/@ Efficiency
t
Design equivalent speedand work output
90xlO3 39
IO0
37
85
35
105 084.4
_- Y 3.6 / _;3.4 _-:_-_1 4.0 i-/3. 2
80
_ 5-<-t-7-h-q701:?_'_S:_937 _5_ _V
31 70-
3. o z.8
29 33
i
6oh
O
25
li
i
-
i
7.6
--. d-- Yd- -t--A=z_
2.4
-4
2.z
I
_._;c.;-t-'.-i'l
55[ _'
f/
--
23 .SO
21
l,'J-5" 7..I.. k Ob / 4 / ._'_ / ,_..-'T
"_
85
_' " / ?1 /"7 _ i" F;.. ,. ;]¢.. >.4:-I-
42.o
_'-.. 70;_.--80-U7 -1/-
"E 19
2
-
P x...t[../,c,(-/_2_._-'1.. /'IV-" /I/--1--/7
40
17
/
i 1.8
I..i.I
u -C,q'-_/- e,--7 ,
15
"i"l
13
30
11
2=. 3
LI -'>
;j-1
___L
7
I
9 4 5 6 7 8 Product of equivalent mass flow and equivalent rotative speed, _wN/6, (kg)iradl/sec 2
lOxlO3
_8
211xl04
9I
I 10
I 11
_ 12
I 13
l 14
_L.... 16 I 15
I 17
i 19
I 18
I 20
Product of equivalent mass flow and equivalent rotative speed, ¢wN/8, (Ibl(rpm)/sec
FIGURE
for
the
same
selected
turbine
to illustrate
12-16.--Turbine
whose
map
certain
performance
is shown
are
shown
ated
with
in mass in figures two
stator
having
figure
12-18
376
flow 12-17
different a large
was
rate and stators.
stagger
obtained
in figure
12-16.
but
were
points. Mass
Variations
map.
with
Flow
with
turbine
12-18
for
Figure angle a stator
pressure
ratio
a single-stage 12-17
(small
was
speed
turbine obtained
stator-throat
having
and
a small
operwith
area), stagger
a and
angle
EXPERIMENTAL
(large
DETERMINATION
stator-throat
identical, In
and
both
rate
area).
the
figures
increases
as
value is reached. increase in mass that
either
mum this
value
the
rate
with In
12-17
would
32
for
the
speed,
by
]arge
choked
speed; maximum indicates the
maxi-
rotational speed. in the rotor inlet
In some
losses
which rotor,
maxi-
causes
cases,
This rela-
however,
a decrease
the
in maxi-
speed.
discussion
a multistage indicate
speed.
the
speed,
of the
the
rotational
12-18,
rotational
incidence
flow
maximum
area,
the
In figure
case
decreasing
mass
some
stator-throat
increases with decreasing and is due to an increase
decreasing
were
choked.
small
the
the
until
is unaffected by
blades
in pressure ratio produces no this maximum in mass flow is
is choked.
For
stator
a given
increases
has
the
rate
the
has
been
turbine,
the
a first-stage
for
the
flow
stator
case
of
variation choke.
a
single-stage
shown A flow
in figure
variation
of
14.5_
31 30
3
rotor
stator
with
foregoing
turbine.
that ratio
is for
flow the
of very
flow
The
which
is choked.
pressure
occurrence mum
or the
flow rate behavior
total
cases,
PERFORMANCE
used.
seen
is influenced
rotor
both
was
pressure
stator
that
mum mass is the usual tive
be
of mass
flow
that
it can
12-17,
indicates
mass
rotor
AERODYNAMIC
A further increase flow. The reason for
the
In figure
For
same the
OF
_
i
E
_:
!
•_ 24
_
14.0_ 13.5_
_
f_
.%_
.... _---__
_spee_
12.o}- /F
o
4o
II.5-
o
60
I0.5
o
II0 I l_i
._
23!
l I, __
22 t 21
t
i
1.4
1.6
I
_
i
I_
1.8 2.0
2.2
2.4
I
1
I
_
3.0
3.2
3.4
3.6
i0.0!
9.5 ' 1.0 1.2
2.6
2.8
3.8
Ratio o1'inlet-total to exit-total pressure, pb/p_ FIGURE
12-17.--Variation of for turbine
equivalent with small
mass flow stator-throat
with area.
total-pressure
ratio
377
TURBINE
I_EISIGN
AND
&PPLZCATION
49 48 47
45
=
44
"E 43 "5
42 41
4O 39 17.5L
1.2
1.3
I
1.4
I
1.5
I
1.6
t
1.7
i
1.8
I
1.9
I
2.0
I
2.1
I
2.2
2.3
Ratio of inlet-total to exit-total pressure, p_/p_ FIGURE
12-18.--Variation turbine
the
type
shown
downstream exactly between
row
stator
at
378
figure
row
row
3.7. flow
the
the
static
about
3.2.
second
rotor
then
It is, of course, the rate for the turbine.
by
For As
ratio static
while
the in
the
particular the
turbine
chokes first
each
the
constant first
are
pressure for
pressure
is indicated
of
some
determine
shown
turbine
to decrease.
for
measurements Such data
is
occurs
in
To
in hub
remaining
choking
ratio
stator.
speed)
blade
continues
to increase,
ratio of about the maximum
variation As
12-19,
a
ratio
choking
static-pressure to be obtained.
turbine. blade
pressure
or
constunt
given
that
with total-pressure area.
indicate
rotor
the
(at
pressure in
a turbine
continues
pressure tablishes
any
of
static
illustrated
would a
where
ratio
in
upstream
downstream
either
of a two-stage
choking
pressure
12-18
12-19,
pressure exit
mass flow stator-throat
choking occurred, rows would have
in figure
turbine
increases,
ratio
row,
where this the blade
blade
case
figure
blade
illustrated with
in
of equivalent with large
at choke
second pressure
a turbine that
es-
EXPERIMENTAL
DETERMINATION
OF
AERODYNAMIC
PERFORMA.__TCE
First stator exit
First rotor exit Second stator chokes Second rotor chokes I Second stator exit
I I
I
I
3.0
3.5
.i 2.0
1.5
2.5
I I I
Second rotor exit
i
l
l
4.0
4.5
Ratio of inlet-total to exit-total pressure, pb/p_ FIGURE
12-19.--Effect
of turbine total-pressure ratio two-stage tu_rbine.
on hub
static
pressure
in a
Torque As
indicated
should
vary
exit
for
any
12-20.
creases
the
AVu
(absolute) with
constant
For torque
tuining
due
in the
rotor.
rotor
increases)
flow
speed,
(exit
ratio
pressure to flow decrease
with
angle
pressure and the
becomes flow
varies
higher
the
in
ratio
in-
values turning
torque in
in inlet
is shown
increased
in mass
change
torque
speed
rate
ratio,
torque
rotor
and
a decrease
the
the
between
tbe
flow
1),
in which and
velocities
is due
absolute
and
(hV_)
manner
mass
high
a possible
rate
2 (vol.
increasing
a given
This
and
The
pressure
the At
speed.
chapter
velocity
to a higher
from
in the
mass
radius.
turbine a given
resulting
increasing
as speed
the
of
of absolute
with
figure
(2-9)
with
component
experimentally
of
equation
directly
tangential and
by
decreases amount
more
of
positive
rate. 379
TURBINE
I_E,SIGN
4000 --
AND
APPLICATI,0N
5500 50O0 /- Design point
4500 32OO ,
E
2800
,.o" 2400 --
g
4OOO
z
Percent of
_o- 3500 C
design equivalent
_" 3000 E o
_ __
1500
g
1290
20 40
0
6o
1500'
A _7 I_.
--
1000'
,4 17
100 110
--
500'
I>
120 130
2500
_ •_ _
--
800 4OO
speed 0 []
o-
o 1.4
1.8
2.2
I
I
I
I
I
2.6
3.0
3.4
3.8
4.2
Ratio of inlet-total FIGURE
12-20.--Variation
of
I 4.6
to exit-static pressure,
equivalent
torque
with
I
I
I
5.0
5.4
5.8
70 80 90
p_IP2
turbine
pressure
ratio
and
speed.
Figure speed,
12-20 the
shows
torque
that
tends
as the
pressure
ratio
off
reach
to level
Above this limit, additional torque.
any further increase This phenomenon
and
indicated
on
ratio
converging
is
pressure specific
work
for each
approached
but
the
area
annulus
axial
Mach
The
flow data.
performance map ratio
efficiency
the
to
not
map
yield
12-16,
reached.
turbine
by
exit
for
value.
ratio results in no "limiting loading"
the
lines
of
value limiting
Limiting is choked;
a given
a maximum
a maximuin
In figure
been
increases
in pressure is termed
performance
speed.
at the
of
constant
equivalent
loading
loading that
is being
occurs
is, when
when the
exit
is unity. and
torque
These
map.
is to select for
has
number
mass
measured
a
and
The
the
are then
usual
mass
various
curves
curves
flow
speeds.
calculated,
just
are then procedure and
torque
Specific and
the
discussed used
can
be plotted
to construct
in constructing at even work,
from turbine
a performance
increments
ideal
performance
the
of pressure
specific map
work,
and
can
be drawn.
of presenting
turbine
Efficiency Another 380
convenient
and
widely
used
method
EXPERIMENTAL
performance _, which
DETERMINATION
is to plot is given
by
OF
efficiency
the
AERODYNAMIC
as a function
PERFORMANCE
of blade-jet
speed
ratio
equation U (12-14) _/2gJ,_h_
where U
blade
mean-section
speed,
m/sec;
Ah_
ideal
specific
based
on
pressure, This
was
J/kg;
discussed for
to vary
speed
an
2 (vol.
idealized
parabolically
Experimentally jet
in figure
of
inlet-total
static
12-21
1), where
case.
with
obtained
ratio
ratio
to
exit-static
Btu/lb
in chapter
mathematically shown
work
ft/sec
For
blade-jet
a correlation that
case,
speed
ratio.
was
shown
efficiency
was
efficiencies
are plotted
against
blade-
for a two-stage
axial-flow
turbine
over
___
<_
50
_
30
a
_q
/ / /
/ /
Design value
.1
I .1
1 .2
I
I
I
I
I
I
.3
.4
.5
.6
.7
.8
Blade-jet
FIGURE
12-21.--V_riation
speed ratio,
of efficiency
with
v
blade-jet
speed
ratio.
381
TURBINE
wide
I)E,SIGN
range
turbine, only jet
of speed
because very
and
AND
and
of the
slightly
are,
therefore,
speed
ratio
generalized
not serves for
be noted,
as for
the
where
limiting
somewhat,
turbine
parameters,
we
The
total
and
very
low
stages
higher
presented.
Figure
very
to
well
a real
turbine
represented
by
this
figure.
is approached, at the
angles should
the blade-jet
Flow
Angles
not
understand
as they
the
ideal always
operating lines
speed
were blade-
efficiency an
this
efficiencies
that
is not For
considered how
static
as for
speed
lower
are
the shows
correlation
for
velocities,
turbine
as well
the
efficiencies exit
than 12-21
correlate
that
loading
flow
two
ratio.
however,
especially
Although
pressure
(1 or 2 percent)
manner
It should
A.PPLI.CATION
tend
in
turbine. as good
conditions to separate
ratios.
turbine
vary
over
performance the
turbine
Percent of design equ ivalent speed
3O
2O --
80
100
10
0 "0
120
_'_ -10 g
2- -2o -30
-40
-50
-6O
1
I
I
I
I
I
1.4
1.6
1.8
2.0
2.2
2.4
Ratio of inlet-total to exit-total pressure, P_P_t FIOURE
382
12-22.--Variation
of rotor
incidence and speed.
angle
with
turbine
pressure
ratio
a
EXPERIMENTAL
operating row to
DETERMINATION
conditions.
determines
the
off-design
incidence inlet
angle,
a range
turbine, angles
the
resultant
herein
defined
of the
velocity
velocity.
The
following
this
figure:
tential
4
which in
entering
each
is an important
chapter
as the
8
contributor
(vol.
difference
blade
2).
The
rotor
the
rotor-
between
the rotor
blade
inlet
angle,
and
pressure
ratio
for
a typical
single-stage
in figure
12-22.
values
are presented
as being
positive
is in the
generalized variation
range
flow
PERFORMANCE
and
vector
(1) a large
operating
loss,
is defined
angle
ponent
of the
discussed
of speed
and are
as
which
flow
direction
incidence
losses,
relative
over
The
OF AERODYNAMIC
when same
of a turbine,
(2) the
com-
the
blade
made
from
be
occurs
change
Flow
as
can
angle
calculated
tangential
direction
observations
in incidence
the
was
over
the
in incidence
po-
angle
Percent of design equivalent speed
m
16-_" A _3 ©
8--
0--
4O 5O 6O 7O 8O 90 100
[] ©
-16 --
o Q_
-2_--
L.
-32 --
-40 --
-48 --
-56 2
1
I
I
I
I
I
t
1.3
1.4
1.5
1.6
1.7
1.8
1.9
I 2.0
] 2.1
Ratio of inlet-total to exit-total pressure, p_/p_, FIGURE
12-23.--Variation
of
outlet
flow speed.
angle
with
turbine
pressure
ratio
and
383
TURBINE
with
I)E,SIGN
pressure
rotor
AND
ratio
incidence
becomes
angle
increases and The turbine
APPLICATION
speed outlet
becomes
angle
12-23
for
graph.
The
angle the
is plotted
over
single-stage
trends
also
to the
in outlet
direction
of speed
Stator
loss
outlet
flow
angle
to that
is
shown
total-pressure trailing of
directly
loss
edge
the
loss
occurs
circumferential such
as shown
trated
near
affected with
by
in figure
the
hub
the
end-wall
increasing
boundary-layer 7 (vol.
2). the
the
_=_
--
1.5
--
in and
12-8.
at
wake
one
region.
The
majority where
boundary
ratio
be noted.
and
loss
of
para-
the incidence being
speed
Once
Suction
the
behind
the seen
stator that
of many
such
total-pressure
of the
traces
ratio
were
concen-
were
greatly
The
pressure
increased flow)
and
total-pressure the
the
end-wall data
as described area
turbine
of one and
--
stator
passage perform-
surface
_c_
__ressure
0
384
12-24.--Typical
total-pressure
loss
survey
data
at
can
in chapter full
One blade pitch
FIGURE
loss
loss
/
su rfac/
all
measurements
,'
o
by
as that
circumferential
composite stator
(and
over
pressure
- (=_ ca. "--
that
is in the
such
be plainly
coefficients
losses
total
just
can
The
.1.0-r,--
in figure last
difference
A typical
of
layers.
velocity
stator.
for
equipment
A
tip regions,
of the
only
radius It
12-25.
can
ratio
to in the
terms
contours
loss for the
2.0
design
angle.
survey
12-24.
to kinetic-energy
total
ratio
to the
pressure
ratio
and
yields
critical
Integration
it)
taken
and
buildup
be converted gives
in
traces
the
Loss
12-7
in figure
the
incidence
probe
survey
is shown
(3)
pressure
respect
made
pressure
measurable
in figures
and
angle,
with
for rotor
of a total-pressure
previously
and
the
referred
generalizations
Stator
means
as with
turbine
and
flow
opposite
positive
is important
a range
observed
apply
change
increases,
may be downstream of the turbine or to the can be obtained from the outlet flow. Outlet
the
same
as speed
more
decreases. flow angle
of whatever component amount of thrust that flow
greater
blade
exit.
EXPERIMENTAL
DETERMINATION
Total-press ure ratio (blade exit to blade inlet_
OF
AERODYNAMIC
PERFORMANCE
Total-pressure ratio (bladeex_t 1o Nade inlet)
v,
>0.98 0 90 to 098 >0.80 to 0.90
E::3 >0 98 090 Io 098 0.80 to 0.90 >070 to 0.80
Pressure surface side Suction surface ,, side -
(b) Total-pressure ratio (blade exit to blade inlet)
Total-pressure ratio (blade exit to blade inlet} r_>
r---I >098 _zza 0,90 to 0.98 i_ 0.80 to 090 I_ 0.70 to 080 _lm >0.60 to 070
0.98 0 90 0.80 0.70 >060
to to to to
0.98 0,90 0.80 070
I I 4
L_j (d_
(c) (a)
Ideal ity
(c)
Ideal ity
FIGURE
after-mix
ratio,
critical
veloc-
critical
veloc-
(d)
0.823. of
obtained
total-pressure
Surface
profiles
Ideal
part
of the
that
yield
ratio
experimentally,
blading favorable
after-mix
ratio,
ity
12-25.--Contours
An important
Ideal ity
after-mix
ratio,
ance have been can be made.
surface
(b)
0.512.
a
critical
veloc-
critical
veloc-
0.671. after-mix
ratio,
0.859.
from
stator
turbine
annular
loss
surveys.
breakdown
Velocity design
is the
surface
selection velocity
of the
blade
distributions. 385
TURBINE
DE'SIGN
Analytical
AND
methods
chapter
5 (vol.
mine
achieved.
During
the
To
the
the
velocity
ments.
With
the
known,
the
velocity
static
pressure
can
v-f_'+i[-1
L_--1L-\p_-/
tribution
shown
Acceleration
on
smooth,
and
no
flow
large
(force
the
the
12-26(a)
suction
maximum is well
a blade
surface,
the
along
surfaces
the
in the
measureblade
from
the
surfaces relation
to
(12-15)
determined surface similar conditions.
is considered
surface
distributed
blade
jj
maximum
along
1.4
the
surface.
one.
velocity
is
There
are
subsonic.
on either
other hand, Flow on
velocity The dis-
to be a desirable
the
is maintained
(diffusions)
12-26(b), on the to be undesirable.
along
( P']'"-"'"7"lr"
velocity
decelerations
on blade)
Figure considered
in figure
to deteractually
be determined
Figure 12-26 shows the experimentally distributions for two stators tested under
in
were
on static-pressure
distribution
distribution
Vc,
along
section
discussed
velocities
distribution
in the
were
it is of interest
surface
are made
previously
velocities
program,
for"
measurements
discussed
surface test
"designed
obtain
static-pressure manner
for calculating
2).
whether
APPLICATION
The
loading
blade.
shows a velocity the suction surface
distribution accelerates
B
1.2
._
>_1.0
r- Suction surface
¢''_\ _ Suction surface
--
_
_.
i,/.....E,/ '
/
•2 _
.Z/
"0 f_).
0.. 3_. _
surface
i
.
I 0
.2
.4
surface
__Pressure .6
I
I_
I
'_ Pressure
I
I
.8 1.0 0 .2 Fraction of blade surface length
I
.6
(a)
(a)
Desirable FIGURE
386
I .8
(b)
distribution. 12-26.--Experimental
I
.4
(b) surface
Undesirable velocity
distribution.
distributions.
I 1.0
EXPERIMENTAL
to
a supersonic
deceleration thickening and face.
could
DETERMINATION
velocity
back
to a subsonic boundary
possibly
lead
A deceleration
result
in reattachment
distributions blades
with
are being
because sharp
and
velocity. layer
observed
of the
flow
of
any
the by
separated and
valleys
causes
increase
off the
pressure an
a rapid
a deceleration
associated
on
PERFORMANCE
undergoes
an
it is followed peaks
then
Such
with
to separation
is also
as critical,
AERODYNAIVIIC
(V/Vcr=l.2)
of the
is not
OF
suction
surface,
acceleration
flow. should
In
sur-
but that
general,
be avoided
a
in loss this
would velocity
when
the
designed.
REFERENCES 1.
DOEBELIN,
ERNEST 0.: Measurement Systems: Application and Design. McGraw-HiU Book Co., 1966. 2. PUTRAL, SAMUEL M.; KOFSKEY, MILTON; AND ROHLIK, HAROLD E.: Instrumentation Used to Define Performance of Small Size, Low Power Gas Turbines. Paper 69-GT-104, ASME, Mar. 1969. 3. MOFFITT, THOMAS P.; PRUST, HERMAN W.; AND SCHUM, HAROLD J.: Some Measurement Problems Encountered When Determining the Performance of Certain Turbine Stator Blades from Total Pressure Surveys. Paper 69-GT103, ASME, Mar. 1969. 4. WISLER, D. C.j AND MOSSEY, P. W.: Gas Velocity Measurements Within a
5.
Compressor Rotor Passage Using 72-WA]GT-2, ASME, Nov. 1972. ASME RESEARCH COMMITTEE ON Theory and Application, 5th ed., Engineers, 1959.
the
Laser
Doppler
FLUXD METERS: The American
Velocimeter.
Fluid Society
Paper
Meters, Their of Mechanical
387
TURBINE
DE,SIGN
AND
APPLICATION
SYMBOLS A
area,
C
discharge
D
diameter,
E
thermal
g hh_d
conversion ideal
m2; ft 2 coefficient m;
ft
expansion constant,
specific
pressure, turbine
J
conversion
K
conversion
M
approach
N
rotative
speed,
P R
absolute
pressure,
absolute
V
absolute change
AVu
work,
absolute
and exit,
kg/sec; angle,
torque,
5'
ratio of specific heat constant volume ratio
of
defined
ratio
from
to
kg/m
annulus
cr
critical
eq in
equivalent meter inlet
std
standard
t
meter
0
measuring
388
be-
or (12-6)
direction,
pressure
pressure
velocity
deg
critical
ratio, 8; lb/ft
defined
condition
by
sea-level
Mach
eq.
1)
condition
throat station
at turbine
standard
inlet
heat sea-level
by eq. (12-12) on
based
by eqs.
3
(at
to
velocity
defined
to specific
based
Subscripts" an
axial
defined
critical
temperature, speed
density,
velocity
ft/sec
at constant total
of
temperature blade-jet
absolute
by eq. (12-5)
pressure function of specific-heatratio,
sea-level
of
lb-ft
turbine-inlet
squared
ft/sec
m/sec;
measured
F
N-m;
(o R)
lb/sec
factor,
flow
m/sec;
m/sec; ft/sec component
inlet
flow rate,
(sec)
(12-4)
K; °R speed,
gas velocity, in tangential
compressibility
(min)/(rev) by eq.
rev/min
temperature,
mass
(rad)
defined
(K) ; (ft) (lbf)/(lbm)
mean-section
Y
to exit-static
N/m S; lb/ft 2
J/(kg)
W
of inlet-total
Btuflb
1 ; 9/30 factor,
rad/sec;
rotor
2)
1; 778 (ft)(lb)/Btu
constant, velocity
tween
on ratio
J/kg;
constant,
gas constant, blade
based
(lbm)(ft)/(lbf)(sec
Btuflb
specific
U
1;32.17
work J/kg;
hh'
T
factor
(12-10)
(12-14)
turbine-inlet on and
standard (12-13)
at
EXPERIMENTALDETERMINATIONOF 1
measuring
station
at stator
2
measuring
station
at turbine
AERODYNAMIC
PERFORMANCE
outlet outlet
Superscript: '
absolute
total
state
389
REPORT r_,_t?,.¢,r_
_r-_
, oll_ct4_f_ i;,,l_,_
,t t_l_;l_._,
,_._r,t,_,r_+,_
i T_,,
_r_f,_r_r,,_,,'_,r_. ,.
r.
_,j*_,_
!2C,t
]
_TI
_,,c,r_'._ ,,v!,r_
DOCUMENTATION
"_e'_. ,_,,_;
;_c,
_,
,in_ _,'_tq,_r,_
, :,
:c, rmpl_llnq _,.,r
r_ducln]
22202.,1_02,
_ncl
_6
_t,,_
r_.._,,._n,:
'_...
;,,_t_,_n
_r._,
:_f,,.,,
PAGE _h_ _'_
_f
2;
_h,rTrOn J'_h_n_on
_.t_n_,_ment
Of
,nl,_rmat_on
_teadquar ind
oMs _o. o7o4-o188 Form Approved S_'nd qr%
Budeet
Ser_
cP._.
` Paperwork
3. REPORT
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.Jny
other
asDect
_epott_, DC
1215
Ot
thi%
]._fferson
2050].
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Publication 5. FUNDING
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SUBTITLE
Turbine
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Prolect
NUMBERS
Application
6. AUTHOR(S)
A.
J. Glassman
7. PERFORMINGORGANIZATION NAME(S) AND ADDRESS(ES) Lewis
Research
Cleveland,
OH
8. PERFORMING ORGANIZATION REPORT NUMBER
Center 44135 R-5666
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has an interest in turbines relatedprJrnarily to aeronautics and space applications. Airbreathing engines provide jet and turboshaft propulsion, as well as auxiliary power for aircraft. Propellantturbines provide rocket propulsion and auxiliary power for space craft. Closed-cycle turbine using inert gases, organic fluids, and metal fluids have been studied forproviding long-duration power for spacecraft. Other applications of interest for turbine engines include land-vehicle (cars, buses, trains, etc.) propulsion power and ground-based electrical power.
In view of the turbine-s_stem interest and efforts at Lewis Research Center, a course entitled "Turbine Design and Application was presented during ]968-69 as part of the ]n-house Graduate Study Program. The course was somewhat rewsed and again presented in 1_72-73. Various aspects of turbine technology were covered including thermodynamic and fluid-dynamic concepts, fundamental turbine concepts, velocity diagrams, losses, blade aerodynamic design, blade cooling, mechanical design, operation, and performance. The notes written and used for the course have been revised and edited for publication. Such apublicaLion can serve as a foundation for an introductory turbine course, a means f-or self-study, or a reference for selected topics. Any consistent set of units will satisfy the equations presented. Two commonly used cons!stent sets of units and constant values are given after the symbol definitions. These are the ST units and the U.S. customary units. A single set of equations covers both sets of units by including all constants required for the U.S. customary units and defimn 8 as unity tho_o not required for the ST units. 14.
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