Conceptual Study of Throttled Operation of Rocket Engine Turbopump�
By Takeshi KANDA
Japan Aerospace Exploration Agency, Kakuda Space Center, Kakuda, Japan
(Received May 2nd, 2012)
Throttled operation of turbopumps of liquid rocket engines is studied analytically. Two types of pressure drops in the
propellant injector are examined, that is, the drop of gas injection and that of liquid injection. Circulation is examined in
relation to throttling to operate the pump in the vicinity of the design condition. An enthalpy increase at the pump
entrance is derived analytically in the circulation system. With the derived analytical relationships, throttled operating
conditions are examined for imaginary LH2 and LOX turbopumps with a LH2/LOX property calculation code. The cir-
culation causes gasification at the entrance of the high-pressure LH2 pump. This does not occur in the mid-pressure LH2
pump or the LOX pump. In the liquid propellant injection system, the unstable region becomes narrower than in the gas
propellant injection. The ratio of the turbine flow rate to the pump flow rate decreases in line with throttling. Throttling
does not degrade the engine specific impulse from the viewpoint of the turbine bleed ratio.
Key Words: Throttling, Rocket Engine, Turbopump, Injection, Circulation
Nomenclature
A: cross-section
C: constant
c0: gas speed at turbine nozzle exit
D: diameter
F: force
g: gravitational acceleration
H: head
h: enthalpy
_mm: mass flow rate
N: rotational speed
p: pressure_QQ: volume flow rate
R: gas constant
r: throttling rate
T : temperature
u: speed
W: power
�: theoretical pump flow coefficient
�: pump flow coefficient
�: ratio of specific heats
�: efficiency
�: density
�: theoretical pump head coefficient
: pump head coefficient
Subscripts
a: turbine entrance
b: turbine exit
c: combustion chamber, throttling by circulation only
e: exit
im: impeller
in: inducer
inj: injection
mn: minimum throttling rate
p: pump
pl: plumbing
r: return flow
s: specific, saturation
t: throat, turbine, total
0: rated design condition
1: pump entrance before mixing
2: pump entrance after mixing in circulation system
3: circulation flow before mixing
4: pump exit
1. Introduction
Liquid rocket engines usually operate according to their
design conditions. Their turbopumps also operate according
to the design conditions, that is, they discharge a design flow
rate of propellant at the design pressure and design rota-
tional speed. Propellant injectors, cooling jacket and valves
also operate at the design flow rate, temperature and pres-
sure except at start and stop transient operations. On the
other hand, throttling of the rocket engines is required in
some operations, for example, powered descent, orbit-to-
orbit transfer, hazard avoidance and hovering. Throttling
can condition acceleration and velocity of a vehicle, espe-
cially for the single-stage-to-orbit vehicle (SSTO), and helps
in optimization of the vehicle trajectory. Throttling has been
investigated and several engines were tested in deep and
shallow throttled conditions.1–14) Throttling is also neces-
sary for the rocket-based-combined-cycle engine (RBCC)
to change its operation to the ramjet mode.15)
In the rocket engine, thrust is proportional to the combus-
tion chamber pressure. Under a specified mixture ratio of
propellants, the chamber pressure is proportional to a pro-� 2013 The Japan Society for Aeronautical and Space Sciences�Presented at the Annual Meeting of JSASS, April 13, 2012
Trans. Japan Soc. Aero. Space Sci.
Vol. 56, No. 1, pp. 49–60, 2013
pellant mass flow rate. In throttling of the rocket engine,
both the mass flow rate and the pressure have to change
simultaneously and proportionally. However, in general,
the flow rate of a pump is proportional to its rotational
speed, while its head is proportional to the square of the
speed. To throttle an engine, therefore, shift of the flow
and head coefficients of the pump is required. The shift of
the coefficients may cause pump operation to be unstable,
where the slope between the flow and head coefficients is
positive.3,11,13) As a result of the shift of the coefficients,
pump efficiency will become lower. To keep operation of
the pump around its design specific speed, a circulation sys-
tem is integrated to the pump for the throttled operation.12,13)
As a result of circulation, the pump operates in the stable
region and its efficiency is kept high. However, temperature
increases at the entrance due to the return flow with higher
enthalpy, and it degrades pump suction performance. It is a
key problem in application of circulation to a cryogenic
pump.
In the present paper, relationships on the turbopump-
related throttling operation of the rocket engine are derived
first. The head required for a pump depends on the injected
propellant condition for the combustion chamber, that is,
gas or liquid. The relationships are derived for these two
cases. Relationships for the circulation and for turbine oper-
ation are also derived. Based on the relationships, operating
conditions are calculated for imaginary LOX and LH2 tur-
bopumps. Based on the calculated results, the turbopump
characteristics in the throttling operation, for example,
temperature of the mixed flow at the entrance of the pump,
stable operating region of the pump and turbine flow rate,
are discussed.
There are several kinds of propellants for the rocket
engine, for example, kerosene and methane. When they
are used for the regenerative cooling, they are injected into
the combustion chamber in gas flow with low density. Pump
power characteristics and the enthalpy increase in the circu-
lation system are similar to those of dense propellant of
LOX, whereas injection-related characteristics are similar
to those of H2 gas. The present results are applied to the
throttling characteristics of these propellants.
2. Relationships in Throttling
The thrust of the rocket engine is proportional to the pro-
pellant flow rates and pressure in the combustion chamber.
To throttle a pump, its operating condition is changed due
to the relationship between the flow and head coefficients.
Otherwise, a flow rate and head of the pump is changed
due to circulation. The throttling of the rocket engine is
proportional to thrust.
r ¼F
F0
�pc
pc0¼
_mmp
_mmp0
ð1Þ
The throttling rate and the ratio of the pressure in the
combustion chamber are also proportional to the flow rate
discharged from the pump in the rocket engine when the
mixture ratio is specified. The definitions of the flow and
head coefficients of the pump are
� ¼_QQp
Ae � up¼
_mmp
�
1
Ae � �Dim � ðN=60Þð2Þ
¼�Hp
up2=g� � ¼ g ��Hp
f�Dim � ðN=60Þg2: ð3Þ
The unit of the rotational speed, N, is rpm. Ae,Dim and up are
the discharge area, impeller diameter and impeller speed at
its diameter, respectively. The change of the pump operating
condition in the �– relationship is equal to change of the
specific speed of the pump. Its definition is
Ns ¼N � _QQp
1=2
�Hp3=4
¼ 60 �Ae
1=2 � g3=4
�Dim
��1=2
3=4: ð4Þ
When the circulation pump system shown in Fig. 1 is
adopted, the relationship between the flow rates is
r �_mmp4
_mmp0
¼_mmp1
_mmp0
¼_mmp2 � _mmp3
_mmp0
: ð5Þ
At the design operation, the flow rate into the pump, _mmp1, is
equal to that discharged from the pump, _mmp4, and they are
equal to the design pump flow rate, _mmp0. There is no circu-
lation flow rate, _mmp3, in the design condition here.
There are two kinds of pressure drops in the propellant
injector of the combustion chamber. One is the drop propor-
tional to the propellant mass flow rate. It appears when gas
propellant, for example, hydrogen gas, is injected. Another
is the drop proportional to the square of the propellant mass
flow rate. It appears when liquid propellant, for example,
liquid oxygen, is injected. Strictly speaking, there is no dis-
tinction between gas and liquid in the supercritical condi-
tion. Herein, low and high density conditions correspond
to gas and liquid conditions, respectively, from the view-
point of the pressure drop in the injector. In both cases, gen-
erally, the pressure drop in the injector should be larger than
15 to 20% of the combustion chamber pressure in order
to avoid combustion instability. A large pressure drop is
required for liquid propellant injectors in the design condi-
tion in order to keep the suitable pressure drop even in the
throttled condition. In the following, the pump discharge
Fig. 1. Pump with circulation.
50 Trans. Japan Soc. Aero. Space Sci. Vol. 56, No. 1
pressure and the throttling condition are examined for each
type of injector pressure drop.
Herein, a mixture ratio is presumed to be fixed at the
design condition. The throttling due to the change of the
mixture ratio is a topic for another study and out of the scope
of this study. A turbine is operated in the coolant bleed cycle
with heated hydrogen after the regenerative cooling.
2.1. Gas injection
2.1.1. Pump characteristics
In the gas propellant injection, the pressure drop is pro-
portional to the propellant flow rate and the combustion
chamber pressure. Assuming that gas in the injector mani-
fold is in the stagnation condition and changes isentropi-
cally, the mass flow rate is written as
_mm ¼ A � Pt
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffi2�
ð� � 1ÞR � TtPc
Pt
� �2�
�Pc
Pt
� ��þ1�
24
35
vuuut¼ A � ð1þ CinjÞPc
�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffi2�
ð� � 1ÞR � Tt1
ð1þ CinjÞ
� �2�
�1
ð1þ CinjÞ
� ��þ1�
24
35
vuuut :
ð6Þ
Here, the ratio of the injector pressure drop to the chamber
pressure, Cinj, is
Cinj ¼�pinj
pc: ð7Þ
Cinj should be held to 0.15 to 0.2 for stable operation. As
shown in Eq. (6), when the ratio of Pc=Pt is fixed, the mass
flow rate is proportional to Pt, differing from the relation-
ship in the liquid injection. Based on Eq. (6), the injector
pressure drop, �Pinj, is written as
�Pinj ¼ Cinj � Pc
¼Cinj
ð1þ CinjÞ
�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið� � 1ÞR � Tt
2�1
ð1þ CinjÞ
� �2�
�1
ð1þ CinjÞ
� ��þ1�
24
35
vuuuuut�_mminj
Ainj
:
ð8Þ
When Cinj and Tt are fixed during throttling, the injector
pressure drop is proportional to the mass flow rate.
When the other pressure drops in the engine are also
proportional to the combustion chamber pressure, the ratio
of pressure increase of �pp=�pp0 in the pump is approxi-
mately proportional to the throttling rate of r.
r ��pp
�pp0ð9Þ
The change of the head in throttling is written based on
Eq. (3).
�Hp
�Hp0
¼ð�pp=�pÞð�pp=�pÞ0
��pp
�pp0�
0
N2
N02
ð10Þ
Density of the incompressible pump fluid is almost constant.
Equation (10) is rewritten for the rotational speed based on
Eq. (9) as
N
N0
�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffi 0
�pp
�pp0
s�
ffiffiffiffiffiffiffi 0
s�ffiffir
p: ð11Þ
The flow rate in the pump in the throttled condition is
written based on Eq. (2).
_QQp2
_QQp0
¼ð _mmp2=�p2Þð _mmp2=�p2Þ0
�_mmp2
_mmp0
��
�0
N
N0
ð12Þ
Equation (12) is rewritten based on Eq. (11) as
_mmp2
_mmp0
��
�0
ffiffiffiffiffiffiffi 0
s�ffiffir
p: ð13Þ
When circulation is adopted, with Eq. (5), the circulated
return flow rate is
_mmp3
_mmp0
¼_mmp2
_mmp0
�_mmp4
_mmp0
��
�0
ffiffiffiffiffiffiffi 0
s�ffiffir
p� r: ð14Þ
Based on Eq. (14), the ratio of circulation in throttling is
defined as
_mmp3
_mmp3c
�
�
�0
ffiffiffiffiffiffiffi 0
r�
ffiffir
p
1�ffiffir
p : ð15Þ
The subscript c represents the throttled condition due to cir-
culation only, that is, the condition where the flow and head
coefficients in throttling are equal to those of the design ones.
The flow rate of the circulation is
_mmp3 ¼ Ar �ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffi2�p3 � r ��pp0
p: ð16Þ
Ar is a cross-section of the circulation return valve. In the
throttled condition, the flow rate in the pump is equal to
or larger than the discharged flow rate.
_mmp4
_mmp0
�_mmp2
_mmp0
ð17Þ
Based on Eqs. (5) and (13), Eq. (17) is rewritten as
r ��
�0
� �2 0
: ð18Þ
When there is no circulation, the sign in Eq. (18) becomes
equal.
There is a specified relationship between and � in a
pump, and is often expressed with a quadratic equation
of �. In the throttled pump with circulation only, the flow
and head coefficients are the same as those at the design con-
dition, and the mass flow rate and rotational speed are a
function of the throttling rate. In the pump with no circula-
tion, when a head coefficient is specified to a flow coeffi-
cient, then throttling rate, rotational speed and pump dis-
charge pressure are derived from Eqs. (18), (11) and (10),
respectively.
Jan. 2013 T. KANDA: Conceptual Study of Throttled Operation of Rocket Engine Turbopump 51
2.1.2. Enthalpy and temperature at pump entrance
Temperature at the pump entrance increases by circula-
tion. Enthalpy of the mixed flow is
ht;p2 ¼_mmp1 � ht;p1 þ _mmp3 � ht;p3
_mmp1 þ _mmp3
¼�0
�
ffiffiffiffiffiffiffi
0
s�ffiffir
p� ht;p1 þ 1�
�0
�
ffiffiffiffiffiffiffi
0
s�ffiffir
p !
� ht;p3
ð19Þ
where ht is the total enthalpy. Power required for the
pump is
Wp ¼ _mmp2ðht;p4 � ht;p2Þ ¼1
�p_QQp ��pp: ð20Þ
The pump efficiency, �p, is a function of � and its estimation
method is explained in the next section. From Eq. (20),
enthalpy at the pump exit is
ht;p4 ¼ ht;p3 �1
�p
�p
�p2þ ht;p2: ð21Þ
Equation (21) is put into Eq. (19), then based on Eq. (9),
ht;p2 � ht;p1 þ�
�0
ffiffiffiffiffiffiffi 0
s ffiffir
p� r
!1
�p
�pp0
�p2: ð22Þ
The temperature of the mixed flow is calculated using
Eq. (22).
2.1.3. Turbine characteristics
In the present study, an impulse turbine is presumed. The
power produced by the turbine is
Wt ¼ �t � _mmtðha � hbÞ
¼ �t � _mmt � Cpt � Ta 1�pb
pa
� ���1�
8<:
9=; ð23Þ
where _mmt, Cpt, and Ta are flow rate, specific heat at constant
pressure and total temperature of the turbine driving gas at
the entrance, respectively. Subscripts a and b indicate the
entrance and the exit of the turbine, respectively. The
efficiency of the turbine, �t, is a function of the ratio of
the turbine blade rotational speed, ut, to the driving gas
speed at the turbine nozzle exit, c0. The ratio is
ut
c0¼
�Dt
N
60ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffi2�
� � 1RTa 1�
pb
pa
� ���1�
8<:
9=;
vuuutð24Þ
where Dt is the diameter of the turbine. The efficiency is
often expressed by a function of the speed ratio.
The turbine gas flow rate is specified in the turbine nozzle
with the choking condition and the rate is proportional to
pressure at the entrance. When the entrance temperature
and the pressure ratio do not change from the design values,
the ratio of the speed ratios is written based on Eqs. (11)
and (24),
ðut=c0Þðut=c0Þ0
¼N
N0
�
ffiffiffiffiffiffiffi 0
s�ffiffir
p: ð25Þ
Changes of the turbine and pump powers by throttling are
Wt
Wt0
¼�t
�t0�
_mmt
_mmt0
ð26Þ
Wp
Wp0
��p0
�p�
_mm2
_mm20
��pp
�pp0: ð27Þ
The power of the turbine is equal to that of the pump. The
required turbine flow rate under throttling is derived using
Eqs. (9) and (13),
_mmt
_mmt0
��t0
�t��p0
�p��
�0
ffiffiffiffiffiffiffi 0
s� r
ffiffir
p: ð28Þ
Using Eqs. (5) and (28), ratio of the turbine gas flow rate to
the pump discharge rate is
_mmt
_mmp4
¼_mmt
_mmt0
�_mmt0
_mmp0
�_mmp0
_mmp4
��t0
�t
�p0
�p
�
�0
ffiffiffiffiffiffiffi 0
s�ffiffir
p�_mmt0
_mmp0
: ð29Þ
Here,
_mmt0
_mmp0
¼�pp0
�p0 � �20�
1
�t0 � Cpt � Ta 1�pb
pa
� ���1�
8<:
9=;: ð30Þ
2.2. Liquid injection
2.2.1. Pump characteristics
Pressure increase required for the pump is
�pp ¼ pc þ�pinj þ�ppl ð31Þ
where �ppl is the pressure drop in plumbing between the
pump exit and the injector, and this drop is presumed to
be proportional to pc.
�ppl ¼ Cpl � pc ð32Þ
The pressure drop in the propellant injector of �pinj is
proportional to the square of the propellant mass flow rate,
that is, the square of the combustion chamber pressure.
�pinj ¼ Kinj � pc2 ð33Þ
In throttling of the rocket engine, the propellant mass flow
rate is proportional to the combustion chamber pressure
shown in Eq. (2). Under a fixed density condition, the mass
flow rate is written as
Pc / _mminj ¼ Ainj
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffi2� ��Pinj
pð34Þ
or
�Pinj ¼1
2�
_mminj
Ainj
� �2
/ Pc2: ð35Þ
When the most throttled condition is designated with a
subscript ofmn, the ratio of the pressure drop to the chamber
pressure is
52 Trans. Japan Soc. Aero. Space Sci. Vol. 56, No. 1
�pinj;mn
pc;mn¼
Kinj � ðpc0 � rmnÞ2
pc0 � rmn¼ Kinj � pc0 � rmn¼ Cinj;mn: ð36Þ
Therefore,
Kinj ¼Cinj;mn
rmn � pc0: ð37Þ
Cinj should be held to 15 to 20% even in the minimum throt-
tling rate. Using Eq. (37), Eq. (33) can be expressed in
another form as
�pinj ¼Cinj;mn
rmn � pc0� pc2 ¼
Cinj;mn
rmn� r2 � pc0: ð38Þ
The pressure increase of the pump of Eq. (31) is rewritten
with Cinj;mn as
�pp ¼ r � pc0 þ ðCinj;mn=rmnÞ � r2 � pc0 þ Cpl � r � pc0
¼ pc0 � ð1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2�
ð39Þand
�pp
�pp0¼
ð1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ: ð40Þ
From Eqs. (10) and (40), the ratio of the rotational speeds is
N
N0
�
ffiffiffiffiffiffiffi 0
s�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
s: ð41Þ
As is in Eq. (13), the pump mass flow ratio is
_mmp2
_mmp0
��
�0�N
N0
��
�0
ffiffiffiffiffiffiffi 0
s�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
s: ð42Þ
The circulation flow rate is
_mmp3
_mmp0
¼_mmp2
_mmp0
�_mmp4
_mmp0
��
�0
ffiffiffiffiffiffiffi 0
s�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
s� r:
ð43Þ
The circulated return mass flow ratio to that in the circula-
tion-only throttling is
_mmp3
_mmp3c
�
�
�0
ffiffiffiffiffiffiffi 0
r�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
s� r
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
s� r
:
ð44Þ
In the throttled condition, the flow rate in the pump is
equal to or larger than the discharge flow rate. From Eq. (42),
r �
�
�0
� �2 0
ð1þ CplÞ
1þ Cpl þ 1��
�0
� �2 0
( )Cinj;mn
rmn
� � : ð45Þ
When there is no circulation, the sign is equal.
2.2.2. Enthalpy and temperature at pump entrance
The enthalpy of the mixed flow at the pump entrance is
ht;p2 ¼_mmp1 � ht;p1 þ _mmp3 � ht;p3
_mmp1 þ _mmp3
�r � ht;p1 þ
�
�0
ffiffiffiffiffiffiffi 0
r ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
s� r
!� ht;p3
�
�0
ffiffiffiffiffiffiffi 0
r ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
s : ð46Þ
Equation (21) is substituted into ht;p3 in Eq. (46), and is rewritten based on Eq. (40) as
ht;p2 � ht;p1 þ1
�p
�pp0
�2
fð1þ CplÞ þ ðCinj;mn=rmnÞ � rgfð1þ CplÞ þ ðCinj;mn=rmnÞg
�
�0
ffiffiffiffiffiffiffi 0
s ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
s� r
!: ð47Þ
2.2.3. Turbine characteristics
From Eqs. (24) and (41), the ratio of the turbine speed ra-
tios is
ðut=c0Þðut=c0Þ0
¼N
N0
�
ffiffiffiffiffiffiffi 0
s�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
1þ Cpl þ ðCinj;mn=rmnÞ
s: ð48Þ
As in Eq. (28), the turbine mass flow rate is rewritten based
on Eqs. (40) and (42) as
_mmt
_mmt0
��t0
�t��p0
�p��
�0
ffiffiffiffiffiffiffi 0
s
�ð1þ CplÞ � r þ ðCinj;mn=rmnÞ � r2
ð1þ CplÞ þ ðCinj;mn=rmnÞ
� �32
: ð49Þ
Based on Eqs. (5), (30) and (49), the ratio of the turbine flow
rate to the pump discharge flow rate is
Jan. 2013 T. KANDA: Conceptual Study of Throttled Operation of Rocket Engine Turbopump 53
_mmt
_mmp4
¼_mmt
_mmt0
�_mmt0
_mmp0
�_mmp0
_mmp4
¼
�t0
�t
�p0
�p
�
�0
ffiffiffiffiffiffiffi 0
r�
ð1þ CplÞr þ ðCinj=rmnÞr2
ð1þ CplÞ þ ðCinj=rmnÞ
� �32
r�_mmt0
_mmp0
:
ð50Þ
The ratio of the turbine flow rate to that of the pump at the
design condition is as shown in Eq. (30).
3. Results and Discussion
Operating conditions of imaginary, throttled LOX and
LH2 pumps are calculated with the relationships for a
1,000 kN-level, high-pressure LOX/LH2 rocket engine
and a 100 kN-level, mid-pressure engine, respectively.
Hydrogen is often injected into the combustion chamber
in low-density after the regenerative cooling. Oxygen is
not usually used for cooling and injected in high density.
Herein, the gas propellant injection is applied to a LH2 sup-
ply system, whereas the liquid propellant injection is applied
to a LOX supply system.
The head coefficient of the imaginary pump is expressed
with a quadratic equation of the flow coefficient. Efficiency
of the pump is calculated based on the following procedure.
The theoretical head coefficient is expressed as16)
� ¼ 1�� � C: ð51Þ
Here, � and � are theoretical head and flow coefficients,
respectively. C is a constant. The =� of an actual pump
reasonably corresponds to � .16) Thus, the pump efficiency
is presumed to have the following relationship in the present
conceptual study.
�¼ 1� � � C ð52Þ
At the design point, the efficiency of �0 is presumed to be a
maximum, specified value. The coefficient of C in Eq. (52)
is specified with the design point conditions.
C ¼1�
0
�0�0
ð53Þ
A two-stage impulse turbine is presumed for the turbo-
pumps. The turbine efficiency is expressed with a quadratic
equation of the speed ratio and becomes largest at the ratio
of 0.25.
Properties of oxygen and hydrogen are calculated with a
code for LOX/LH2 rocket engines.17) Total pressure of the
mixed flow, pt2, is presumed to be equal to pt1.
Presumed specifications of LH2 turbopumps are listed in
Table 1 and those of LOX turbopumps are listed in Table 2.
The LOX turbopumps are designed at the minimum throt-
tled condition of 10%. As shown in Eq. (39), the pressure
drop in the injector becomes larger at the design condition
as the minimum throttling ability is set to be smaller, and
the pump discharge pressure becomes much higher in a deep
throttling engine. The features and problems in throttling
with the liquid propellant injection are made clear in such
a deeply throttled engine. The design pump discharge pres-
sure is approximately 40MPa under the combustion cham-
ber pressure of 15MPa in the high-pressure engine, listed
in Table 2. CECE has a throttling ability of 10 : 1 and the
high delta pressure injector for LOX.4)
In the examination of the LH2 supply system, the pump
discharge pressure is set to 20MPa for the 1,000 kN-level
engine and 5MPa for the 100 kN-level engine referring to
the LE-5B and LE-X engines.18,19) In the examination of
the LOX supply system, the ratio of the pressure drop in
plumbing to the chamber pressure, Cpl, is set to be
0.15.18–20) The ratio of the injector pressure drop to the
chamber pressure, Cinj, is 0.15.
Figure 2 shows head coefficient and pump efficiency of
LH2 imaginary pumps, and Fig. 3 shows those of LOX
pumps.
Table 1. Specifications of LH2 turbopumps at design condition.
1,000 kN-level, high-pressure engine
Combustion chamber pressure, MPa 15
H2 pump
Inflow temperature, Tt1, K 21
Inflow pressure, Pt1, MPa 0.3
Flow rate, kg�s�1 40
Efficiency 0.8
�P0, MPa 19.7
Entrance diameter, m 0.18
Impeller diameter, m 0.24
Rotational speed, rpm 50,000
Specific speed, m, m3/m, rpm 132
H2 turbine
Rotor diameter, m 0.22
Temperature at entrance, K 500
Pressure ratio 8
Efficiency 0.5
100 kN-level, mid pressure engine
Combustion chamber pressure, MPa 3.5
H2 pump
Inflow temperature, Tt1, K 21
Inflow pressure, Pt1, MPa 0.3
Flow rate, kg�s�1 3.5
Efficiency 0.8
�P0, MPa 4.7
Entrance diameter, m 0.07
Impeller diameter, m 0.15
Rotational speed, rpm 50,000
Specific speed, m, m3/m, rpm 113
H2 turbine
Rotor diameter, m 0.16
Temperature at entrance, K 400
Pressure ratio 5
Efficiency 0.5
54 Trans. Japan Soc. Aero. Space Sci. Vol. 56, No. 1
3.1. Pump characteristics
Figure 4 shows operating conditions of the LH2 pumps in
line with throttling for the no-circulation and the full-circu-
lation conditions. Figure 5 shows those of the LOX pumps.
In the full-circulation condition, the flow and head coeffi-
cients are fixed at the design values during throttling. The ro-
tational speed and the pump discharge flow rate decreases in
line with the throttling rate. In the no-circulation condition,
the flow coefficient also decreases. The head coefficient does
not change greatly during throttling. Unstable in the figures
is shown as the region of the positive slope in �– relation-
ship. The normalized features of the two LH2 pumps are al-
most the same except for the unstable operating area even
though the head coefficients and efficiencies are different
as shown in Fig. 2. This similarity is also seen in LOX pumps.
In the LH2 pumps, the rotational speed shows convex
change in line with throttling. As shown in Eq. (11), the ro-
tational speed is proportional to the square roots of the throt-
tling rate and the head coefficient. The head coefficient is
fixed at the design value in the full-circulation condition
Table 2. Specifications of LOX turbopumps at design condition. Mini-
mum throttling is 10%.
1,000 kN-level, high-pressure engine
Combustion chamber pressure, MPa 15
Injector pressure drop ratio, Cinj 0.15
Plumbing pressure drop ratio, Cpl 0.15
O2 pump
Inflow temperature, Tt1, K 90
Inflow pressure, Pt1, MPa 0.3
Flow rate, kg�s�1 230
Efficiency 0.8
�P0, MPa 39.5
Entrance diameter, m 0.15
Impeller diameter, m 0.25
Rotational speed, rpm 20,000
Specific speed, m, m3/m, rpm 152
O2 turbine
Rotor diameter, m 0.25
Temperature at entrance, K 400
Pressure ratio 2.5
Efficiency 0.5
100 kN-level, mid-pressure engine
Combustion chamber pressure, MPa 3.5
Injector pressure drop ratio, Cinj 0.15
Plumbing pressure drop ratio, Cpl 0.15
O2 pump
Inflow temperature, Tt1, K 90
Inflow pressure, Pt1, MPa 0.3
Flow rate, kg�s�1 20
Efficiency 0.8
�P0, MPa 9.0
Entrance diameter, m 0.07
Impeller diameter, m 0.15
Rotational speed, rpm 16,000
Specific speed, m, m3/m, rpm 109
O2 turbine
Rotor diameter, m 0.18
Temperature at entrance, K 300
Pressure ratio 2.5
Efficiency 0.5
(a)
(b)
Fig. 2. Head coefficient and efficiency of LH2 pumps.
(a) High-pressure engine. (b) Mid-pressure engine.
(a)
(b)
Fig. 3. Head coefficient and efficiency of LOX pumps designed for 10%
throttling.
(a) High-pressure engine. (b) Mid-pressure engine.
Jan. 2013 T. KANDA: Conceptual Study of Throttled Operation of Rocket Engine Turbopump 55
and does not change greatly in the no-circulation condition
as shown in Fig. 2. So the rotational speed is approximately
proportional to the square root of the throttling rate. In the
LOX pumps, the rotational speed ratio changes more line-
arly proportional to the throttling rate. As the design mini-
mum throttling rate, rm, becomes lower in the liquid propel-
lant injection system, the term Cinj;mn=rmn becomes larger in
Eq. (41) and the rotational speed changes almost linearly to
the throttling rate.
According to Eq. (14), in the no-circulation condition of
_mmp3 ¼ 0, the flow coefficient is approximately proportional
to the square root of the throttling rate in the gas propellant
injection system. In the liquid propellant injection system,
the flow coefficient changes more slowly in line with throt-
tling until approximately r ¼ 0:3. When there is no circula-
tion, Eq. (43) can be rewritten as
�
�0�
ffiffir
p
ffiffiffiffiffiffiffi 0
r�
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffið1þ CplumbÞ þ ðCinj;mn=rmnÞ � rð1þ CplumbÞ þ ðCinj;mn=rmnÞ
s ð54Þ
whereas Eq. (14) of the gas injection is rewritten as
�
�0�
ffiffir
p,, ffiffiffiffiffiffiffi
0
s: ð55Þ
Since the flow coefficient changes more slowly in line with
the throttling rate under the liquid propellant injection sys-
tem in the shallow throttling region, the unstable operating
limit appears lower in the throttling rate than in the gas pro-
pellant injection system. This feature becomes clearer as the
design minimum throttling rate becomes lower in the liquid
propellant injection system. The liquid propellant injection
system has wider stable operating region in throttling than
the gas injection system from the viewpoint of the change
of the flow coefficient.
In the gas propellant injection system with full circula-
tion, the ratio of the circulation flow rate to the pump dis-
charge rate reaches the largest value of 0.25 at r ¼ 0:25 in
the full-circulation condition, as derived by differentiating
Eq. (14). In the liquid injection system, the maximum value
becomes smaller at a smaller throttling rate.
The pumps can operate between no circulation and the
full circulation. Figure 6 shows the 25% throttled condition
(a)
(b)
Fig. 4. Rotational speed, flow rates and coefficients of LH2 pumps in
throttling.
(a) High-pressure engine. (b) Mid-pressure engine.
(a)
(b)
Fig. 5. Rotational speed, flow rates and coefficients of LOX pumps de-
signed for 10% throttling in throttling.
(a) High-pressure engine. (b) Mid-pressure engine.
56 Trans. Japan Soc. Aero. Space Sci. Vol. 56, No. 1
for the LH2 high-pressure pump, and Fig. 7 shows the 10%
condition for the LOX high-pressure pump. �=�0 ¼ 1 indi-
cates full-circulation operation, whereas the left end of
the lines indicates no-circulation operation. In the high-
pressure engine, the operating region of the LH2 pump is
limited not only by the unstable region, but also by the
vaporization region. The region is due to the return flow
of high-enthalpy fluid at the pump entrance. In the mid-
pressure LH2 pump, the increase of enthalpy is smaller,
and this limitation does not appear. The vaporization due
to circulation is discussed in next section. The rotational
speed does not change greatly due to circulation since
0= is almost constant in the throttling region. The pump
efficiency becomes lower for a lower circulation ratio due
to its separation from the design operating condition. At
the same time, however, the pump flow rate becomes small-
er for a lower circulation rate.
3.2. Temperature of mixed flow and suction perfor-
mance
In throttling, the increase of temperature of the mixed
flow at the entrance of a cryogenic pump is a problem for
suction performance in the circulation system. Figure 8
shows temperatures at the entrance and the exit of the
full-circulation LH2 pumps, and Fig. 9 shows temperatures
at the entrance and the exit of the full-circulation, high-pres-
sure LOX pump.
In the high-pressure LH2 pump, the mixed flow at the
entrance is at the saturation temperature under the pump
entrance pressure. This is caused by a large increase of
enthalpy in the low-density hydrogen pump. In the LOX
pump, however, the temperatures at the entrance and exit
do not change greatly from the temperature at the design
point at r ¼ 1, even though the pump discharge pressure
is high. This is caused by large density of oxygen and a
small increase of enthalpy in the pump even though the
pump discharge pressure is very high. In the mid-pressure
LH2 pump, the increase of enthalpy is smaller and the tem-
perature does not reach the saturation temperature. Temper-
Fig. 6. 25% operation of LH2 pump of high-pressure engine.
�=�0 ¼ 1 indicates the full-circulation operation and the left end of the
lines indicates the no-circulation operation.
Fig. 7. 10% throttling operating condition of LOX pump of high-pressure
engine.
�=�0 ¼ 1 indicates the full-circulation operation and the left end of the
lines indicates the no-circulation operation.
(a)
(b)
Fig. 8. Temperature at the entrance/exit of LH2 pumps with the full-cir-
culation throttling system.
(a) High-pressure engine. (b) Mid-pressure engine.
Fig. 9. Temperature at the entrance/exit of high-pressure LOX pump de-
signed for 10% throttling with the full-circulation throttling system.
Jan. 2013 T. KANDA: Conceptual Study of Throttled Operation of Rocket Engine Turbopump 57
ature at the exit shows a strange change. This is caused by a
quick change of properties around the critical pressure. It
may be true or it may be due to the accuracy of the property
calculation code. The effect of circulation on the suction
performance depends on properties of the pump fluid.
Figure 10 shows the net positive suction head (NPSH)
and the cavitation parameter under the full-circulation oper-
ation of the mid-pressure LH2 pump. Herein, their defini-
tions are
NPSH ¼Pt2 � Ps
�2 � gð56Þ
CP ¼P2 � Ps
ð1=2Þ�2 � ui2: ð57Þ
Here, ui is the tip speed of the pump inducer, and Ps is sat-
uration pressure at Tt2. NPSH decreases in line with throt-
tling in the shallow throttling region. In the full-circulation
condition, the saturation pressure increases with an increase
of the temperature of the mixed flow. This decreases NPSH.
As for the cavitation parameter, the rotational speed and the
dynamic pressure become smaller in line with throttling.
This causes the cavitation parameter to increase in line with
throttling.
Figure 11 shows NPSH and the cavitation parameter of
the mid-pressure LH2 pump at the 25% throttling condition.
The point at �=�0 ¼ 1 indicates operation at full circulation,
and the left end of the lines indicates operation with no cir-
culation. Due to the decrease of the circulation flow ratio,
both NPSH and the cavitation parameter increase. However,
the decrease of the ratio causes a shift of the �– operating
condition and makes pump operation unstable. For a LOX/
LH2 engine, for example, shifting the mixture ratio is a
method of producing deeply throttled operation and avoid-
ing unstable operation and gasification.
Figure 12 shows NPSH and the cavitation parameter of
the LOX pump of the high-pressure engine. Due to an in-
crease of the saturation pressure by an increase of tempera-
ture of the mixed flow, NPSH slightly decreases toward
r ¼ 0:3. Even though this feature appears clear in the
high-pressure engine pump, it is a small change. The cavita-
tion parameter increases in line with throttling, as does that
of the LH2 pump.
Figure 13 shows NPSH and the cavitation parameter at
the 10% throttling condition. The point at �=�0 ¼ 1 indi-
cates operation at full circulation and the left end of the lines
indicates operation with no circulation. At 10% throttling,
the unstable region appears in the small flow coefficient
region. The region does not appear in 25% throttling. This
slow appearance of the unstable region in throttling is caused
by the slow decrease of the flow coefficient in line with the
throttling rate in the liquid propellant injection system, as
explained in 3.1. Circulations are effective in a LOX pump
when deeply throttled operation is required, because gasifi-
cation only occurs to a small extent as a result of circulation.
When propellant with large density, for example, a kind
of kerosene or alcohol, is used for cooling and injected into
the combustion chamber in a gas condition, the pump sys-
tem with the propellant has features similar to the LH2 pump
system in operation because of gas injection into the com-
bustion chamber, and features similar to the LOX pump in
temperature and suction performance at the pump entrance
because of high density of the propellant in the pump. The
pump discharge pressure does not become so high and tem-
Fig. 13. NPSH and cavitation parameter of the high-pressure LOX pump
designed for 10% throttling.
Fig. 10. NPSH and cavitation parameter of the full-circulation LH2 pump
of the mid-pressure engine. Fig. 11. NPSH and CP of LH2 pump at 25% throttled condition of the
mid-pressure engine.
Fig. 12. NPSH and cavitation parameter of the high-pressure, full-circu-
lation LOX pump designed for 10% throttling.
58 Trans. Japan Soc. Aero. Space Sci. Vol. 56, No. 1
perature of the mixed flow increases little in the circulation
system.
3.3. Turbine characteristics
Figure 14 shows operating conditions of the LH2 tur-
bines, and Fig. 15 shows those of the LOX turbines de-
signed at the minimum throttling rate of 10%. Though the
LOX pump discharge pressure of the high-pressure engine
is high, the ratio of _mmt= _mmp4 is less than 0.07. The ratio is
within the scope of the turbine bleed ratio. The deeply throt-
tled operation is possible in the LOX supply system.
The turbine efficiency shows little difference due to the
ratio of circulation. The efficiency depends on the speed ra-
tio in the present study. The rotational speed shown in
Eq. (11) does not change greatly as a result of circulation,
since the pump 0= does not change greatly even in the
no-circulation system. Thus, the efficiency does not change
greatly due to the ratio of circulation. In line with throttling,
the turbine efficiency decreases with a decrease of the rota-
tional speed.
The ratio of the turbine gas flow rate to that discharged
from the pump, _mmt= _mmp4, does not become 0 due to the de-
crease of the throttling rate in the full-circulation system.
In the gas injection system, the ratio is a function of the tur-
bine efficiency and the throttling rate as is shown in
Eq. (29). The efficiency is a quadratic function of the speed
ratio and this ratio is the function of the square root of the
throttling rate as is shown in Eq. (25). Thus, the efficiency
is almost linear to the square root of the rate in the deeply
throttled condition. Thus, _mmt= _mmp4 of Eq. (29) becomes a val-
ue in the throttling rate of 0. In the liquid injection system,
when the throttling rate is small, the efficiency is almost pro-
portional to the square root of the throttling rate and _mmt= _mmp4
of Eq. (50) also becomes a value in the throttling of 0. In the
no-circulation system, the flow coefficient in Eqs. (29) and
(50) decreases in line with throttling, and _mmt= _mmp4 becomes
0 for the throttling rate of 0.
Since the pump flow rate becomes larger as a results of an
increase of the circulation rate, the turbine flow ratio of
_mmt= _mmp4 also becomes larger in the full-circulation condition
(shown by a broken line) than that in the no-circulation con-
dition (shown by a solid line). However, the ratios of both
the full- and no-circulation systems decrease in line with
throttling in both the LH2 and LOX turbines. The turbine
gas does not contribute to thrust production greatly and an
increase of the turbine gas flow rate degrades the engine spe-
cific impulse in the bleed cycle. The decrease in _mmt= _mmp4 in
line with throttling indicates that throttling does not degrade
the engine specific impulse from the viewpoint of turbine
operation. Attention should be paid to the fact that the pump
and turbine operating characteristics are modeled here. For
example, when the pump efficiency is much smaller than
the value used here, _mmt= _mmp4 becomes much larger as seen
in Eqs. (29) and (50). Then, the specific impulse may be de-
graded.
Figure 16 shows 25% operation of the LH2 turbine of the
high-pressure engine, and Fig. 17 shows 10% operation of
the LOX turbine of the high-pressure engine. The circulation
ratio decreases with a decrease of �=�0, and the left end of
the lines shows operation with no circulation. Though the
flow coefficient has no direct relationship to the turbine op-
eration, the ratio of the coefficients is used here for compar-
ison with figures of the throttled pump operating conditions.
As mentioned above, the efficiency does not change
greatly due to circulation. The pump efficiency becomes
(a)
(b)
Fig. 14. LH2 turbine operation in throttling.
(a) High-pressure engine. (b) Mid-pressure engine.
(a)
(b)
Fig. 15. LOX turbine operating conditions designed for 10% throttling.
(a) High-pressure engine. (b) Mid-pressure engine.
Jan. 2013 T. KANDA: Conceptual Study of Throttled Operation of Rocket Engine Turbopump 59
lower with a decrease of the circulation ratio due to off-de-
sign operation, but the pump flow rate also becomes smaller.
As a result, the required turbine power, that is, the turbine
flow ratio of _mmt= _mmp4, becomes smaller with a decrease of
the circulation ratio.
4. Concluding Remarks
A conceptual study of the throttling of rocket engine tur-
bopumps was conducted. Relationships between the throt-
tling rate, flow rates, pressure and temperature of the pump
and turbine were derived. The relationships under the gas
propellant injection were applied to an imaginary LH2 tur-
bopump system, whereas those under the liquid injection
were applied to a LOX turbopump system.
In the LOX pump of the liquid propellant injection sys-
tem, the pump unstable region was limited to the deep throt-
tling region, compared to the region of the gas injection sys-
tem for the LH2 pump. This was caused by the slow change
of the flow coefficient in line with throttling in the liquid in-
jection system.
In the high-pressure LH2 pump with the circulation sys-
tem, gasification occurred at the entrance of the pump due
to low density of hydrogen and the large enthalpy increase
in the pump. In the LOX pump or the mid-pressure LH2
pump, temperature at the entrance changed slightly because
of a small increase of enthalpy.
In both the gas injection and the liquid injection cases, the
ratio of the turbine flow rate to that discharged from the
pump decreased in line with throttling. Throttling did not
degrade the engine specific impulse from the viewpoint of
the turbine operation in throttling.
Acknowledgments
The author is grateful to Mr. Tomoyuki Hashimoto of JAXA for
advice and discussion.
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60 Trans. Japan Soc. Aero. Space Sci. Vol. 56, No. 1