study on the simulation method of ...lin491/pub/glin-16-icef.pdfcompressor, the simulation method...
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Corresponding author: [email protected] 1 Copyright © 2016 by ASME
Draft Proceedings of the ASME 2016 Internal Combustion Fall Technical Conference
ICEF2016
Oct 9-12, 2016, Greenville, SC, USA
ICEF2016-9420
STUDY ON THE SIMULATION METHOD OF COMPRESSOR AREODYNAMIC NOISE
BASED ON CFD AND IBEM
Liu Chen College of Power and
Engineering, Harbin Engineering University
Harbin, Heilongjiang, China
Cao Yipeng* College of Power and
Engineering, Harbin Engineering University
Harbin, Heilongjiang, China
Guang Lin School of Mechanical
Engineering, Department of Mathematics, Purdue University
West Lafayette, Indiana, United States
Sun Wenjian College of Power and
Engineering, Harbin Engineering University
Harbin, Heilongjiang, China
Zhang wenping College of Power and
Engineering, Harbin Engineering University
Harbin, Heilongjiang, China
Ming pingjian College of Power and
Engineering, Harbin Engineering University
Harbin, Heilongjiang, China
ABSTRACT Turbocharger compressor aerodynamic noise has been one
of the major noise sources of diesel engine. It is necessary to
study the characteristics of turbocharger fluid flow and radiation
noise for its effective noise control. In this paper, a new for
predicting compressor aerodynamic noise is presented, which
combined the calculated fluid dynamic (CFD) and indirect
boundary element method (IBEM. The unsteady viscous flow in
compressor was simulated based on the finite volume method.
In addition, the periodic pressure fluctuation of the rotor inlet
and blades were used to compressor radiation noise field
simulation by indirect boundary element method (IBEM). In
order to prove the feasibility of numerical simulation, the
acoustics experimental device for compressor aerodynamic
noise experiment was built and the sound pressure of
turbocharger were tested. The trend of simulation results and
amplitude level in blade passing frequency (BPF) coincide with
the experiment results. It indicates that the coupling method is
more effective and accurate in turbocharger noise prediction.
Key words: compressor; CFD; IBEM; aerodynamic noise
NOMENCLATURE
1 2 3, ,L L L the length of the reference body
V the inner area of the closed wall
V the outer area of the closed wall
Z compressor main blades number c sound velocity
d measuring distance
f sound wave frequency
BPFf blade passing frequency
k turbulent kinetic energy
0k sound wave number
n rotation speed
n the wall direction vector p the time harmonic external sound source
( , ,z)q x y volume velocity per unit volume density
0 static medium density fluid dynamic viscosity
angular frequency turbulent dissipation rate
a the boundary of indirect boundary element
region
INTRODUCTION Turbochargers are of great use in turbocharging diesel
engine of vehicles and power stations. The turbocharger
pressure ratio has been increasing due to the requirement of
higher engine power output, which causes the load of
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turbocharger components become higher as well as sound
pressure level of radiated noise of turbocharger. The excessive
noise has been one of the most important problems, which not
only increases the environmental pollution, but does harm to the
health of operators. Thus, it is necessary to study the noise
characteristics of turbocharger for the noise control.
Experimental and analytical methods have been presented
to study the characteristics of turbocharger noise and the effects
of structure parameters on the sound pressure level [1]. In
experimental study, the testing bench will be designed, built and
the accurate results can be obtained. Joachim once reported on
an experimental and numerical investigation aimed at
understanding the mechanisms of rotating instabilities in a low
speed axial flow compressor [2]. Raitor and Neise completed an
experimental study to explore the dominant sound generation of
the spectral components governing the overall noise level of
centrifugal compressors [3]. J. Galindo researched the influence
of tip clearance on flow behavior and noise generation of
centrifugal compressors in near-surge conditions, a correlative
experiment was completed to verify his numerical analysis
[4]. However, the experimental method will meet some
problems at the same time. The testing data contains large
amount information which is not related with the analysis and
need filter. The test is very tough when there are several
different working conditions, research objects, which may cause
time-consuming and laborious shortcomings, and so on. The
most important part of experimental method is that the
characteristic research of turbocharger is after the design
process.
The analytical method can be adopted for analyzing
different research objects, even the object that experimental
research can’t be carried out. The calculation method needs to
be carefully analyzed and selected, so that the result of the
calculation is sufficiently accurate. Sitki Uslu carried out
simulation of noise generation due to blade row interaction in a
high speed compressor [5]. Chu, S. and Dong, R. has done a lot
of work about unsteady flow, pressure fluctuation and noise
associated with the blade tongue interaction in a centrifugal
pump [6, 7]. The effects of structure parameters of compressor
on noise have been studied by various methods. Jeon calculated
the effects of design parameters on performance and noise of a
centrifugal fan [8], he also studied on the noise reduction
method of a centrifugal compressor [9]. Langthjem studied
flow-induced noise in a two-dimensional centrifugal pump [10].
Moreland studied the housing effects on centrifugal blower
noise [11]. Chehhat Abdelmadjid researched the effect of volute
geometry on the turbulent Air flow through the turbocharger
compressor [12]. Hyosung Sun had done a lot of work in
analysis and optimization of aerodynamic noise in a centrifugal
compressor, the simulation method (it is named traditional
method in this paper) can calculate the sound pressure level of
BPF noise and its harmonics [13, 14].
It is widely known that the turbocharger noise level is
dominated not only BPF noise spectrum, but continuous
broadband spectrum. An experimental result was selected as
example and its spectral components are decomposed, the
sound pressure level (SPL) of each component was showed in
Table 1.
Table 1. Spectral component decomposition
Spectral
component
BPF
spectrum
Continuous
broadband
spectrum
Full
spectrum
SPL(dB) 98.25 99.27 101.8
It can be found that the BPF spectral component can’t
represent the total noise level accurately, which means the
traditional BPF method is not comprehensive enough, more
effective methods should be proposed in the compressor noise
prediction. As mentioned above, the coupling method
combining CFD and IBEM is presented in compressor
aerodynamic noise prediction. On the basis of present research,
the prediction range was expanded from fixed frequency points
to the whole frequency band of interest. The feasibility of
numerical simulation method was verified by compressor
aerodynamic noise experiment.
1. NUMERICAL SIMULATION
1.1 Computational model The turbocharger aerodynamic noise can be divided into
two parts, the compressor noise and turbine noise. Because the
turbine is connected with exhaust pipeline which is always
connected with exhaust muffler, the turbine noise can’t radiate
to the air directly. The compressor noise is the main noise
source of turbocharger. In this paper, JTH150 turbocharger is
selected as the research object, there are 8 main blades and 8
split blades, as well as 11 diffuser blades. The three-
dimensional compressor model is shown in Fig.1 (a). The
calculation model of the compressor includes the following four
parts: inlet section, rotor section, stator section and volute
section. The single channel and periodic boundary are used in
rotor and stator flow calculation and the main calculation field
is divided into hexahedral mesh. Unstructured tetrahedral
meshes are used in the inlet section and the flow passage of the
volute section. The computational model used in numerical
simulation is shown as Fig.1 (b) and (c).
(a) The 3-D model
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(b) Numerical simulation model
(c) Numerical simulation mesh
Figure 1. JTH150 compressor model
1.2 Flow field analysis Computational fluid dynamics has been quite mature in the
unsteady flow field analysis [15-17]. In this paper, in order to
adapt to the complicated flow field of the compressor and
ensure the accuracy of the flow field calculation result, the
implicit RNG k double equations turbulent model were
used. The governing equations and the parameters in the
equation are shown in Eq.(1)-(3).
i
k eff k
i j j
k ku kG
t x x x
(1)
2
1
2
i
eff k
i j j
u CG C
t x x x k k
(2)
2
0
1 1 3
1 2
1/2
0
0.0845, 1.39
1 /
1
1.42, =1.68
= 2
1
2
4.377, =0.012
eff t
t
k
ij ij
ji
ij
j i
kC
C
C C
C C
kE E
uuE
x x
(3)
In order to compare with the experimental results later, the
experimental boundary condition is used directly for the
numerical simulation, shown in Table 2.
Table 2. The calculating condition
Working
condition
Rotation
speed(rpm)
Mass
flow(kg/s)
Pressure
ratio
1 36913 0.69 1.67
The method presented in this paper should calculate the
pressure characteristic of compressor flow fluid, so the steady
flow field data would be calculated firstly, and then the data will
be used as the initial flow field to calculate the unsteady flow
field. The pressure fluctuation data on the rotor inlet surface
was extracted, and then the data can be used as sound source
information for further numerical calculation of aerodynamic
noise of compressor.
Figure 2-4 were the compressor pressure、temperature
and density contour, respectively. Figure 2 showed that static
pressure gradually increased from the compressor inlet to outlet.
At the same time, gas temperature in the compressor also
increased significantly, as shown in Fig.3; in Fig.4, it could be
seen that gas density distribution inside the compressor showed
a significant increasing trend from the compressor inlet to
outlet. These figures told that compressor could increase the gas
pressure and gas density in the process of centrifugal
compressor, which indicated the compressor performance
ability.
As the main parts of centrifugal compressor, the rotor
blade would transform the compressor mechanical energy into
gas pressure energy and kinetic energy. Under the centrifugal
force action, the gas rotates at high-speed with rotor, which
causes the gas pressure and density increasing, and the gas
kinetic engine also increases accordingly. Figure 5 showed that
the compressor flow speed is increased and reached its
maximum value at the outlet surface of rotor.
In Fig. 2, the static pressure on the inlet surface of the
diffuser is large smaller than the outlet surface’s pressure, and it
could also be seen that the static pressure on the surface of the
diffuser is significantly increased. With the increasing of the
volute flow channel cross-sectional area, the pressure amplitude
on volute surface is slowly increasing. The Fig.3 shows that gas
temperature has an increasing trend in vane diffuser and volute,
the peak value appears in volute.
Figure 2. Pressure contour
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Figure 3. Temperature contour
Figure 4. Density contour
Figure 5. Velocity streamline
The main function of the flow passage is to convert the
kinetic energy of the air flow into the pressure energy, the
streamline form of gas in the flow passage of the volute is in a
spiral shape. The air flow velocity in the vane diffuser is
decreasing continuously, but the static pressure is increased
gradually.
1.3 Sound field analysis The boundary element method (BEM) is not based on the
compact sound source hypothesis, but uses the "singularity"
processing method, therefore, the boundary element method
does not need to distinguish the acoustic far field and near field.
Theoretically, it can solve the sound field of any position [18-
20]. The specific idea of BEM for solving the sound field is as
follows; the BEM method transforms the differential equation
of the computational acoustic field domain to the discrete
integral equation of the domain boundary, and uses the
weighted method to calculate the integral value on the
boundary.
In this paper, the Helmholtz equation is adopted in the
BEM method to solve the acoustic field. The steady sound
pressure in the acoustic region is generated by the contribution
of the time harmonic external sound source p , the
inhomogeneous Helmholtz equation is:
2 2
0 0, , , , , ,p x y z k p x y z j q x y z (4)
/ 2 /k c f c (5)
Figure 6. Indirect boundary element region
Two fluid regions are defined as shown in Fig.6. V is the
inner region of the closed wall, and V is the outer area of the
closed wall. Based on the front definition of the wall direction
vector n , the direction of the non-boundary area is positive.
The pressure and pressure gradient along the positive direction
of the wall are ap r and ap r n , on the contrary, the
pressure and pressure gradient along the wall of the wall
are ap r and ap r n .
A general indirect boundary integral formula is used, which
can be applied to the external sound field with open boundary
or the combination of both internal and external fields. The
formula can be written as:
,
,
a
a
a a a a
G r rp r r r G r r d r
n
(6)
In the Eq.(6), the single layer potential is the difference of the
pressure gradient on both sides of the boundarya :
a a
a
p r
n
p
n
rr
(7)
The double layer potential is the difference of the pressure on
both sides of the boundarya :
a a ar p r p r (8)
The single layer potential can be regarded as a monopole
sound source distribution of the boundary interface, and the
double layer potential can be regarded as the dipole source
distribution of the boundary interface.
The boundary element model of the inlet pipe and the rotor
of the compressor is shown in Fig.7 (a), you could have a more
direct view of the boundary element mesh from another
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perspective in Fig.7 (b). In order to consider the acoustic
transmission without consider the acoustic reflection, rotor
outlet surface is set to a non-reflecting boundary.
(a) Mesh schematic diagram
(b) Section view
Figure 7. BEM mesh
Figure 8. Field point mesh
The field point mesh is established as a box shaped
envelope, shown in Fig.8. Nine sound pressure reference points
are selected on the surface or the edge of envelope. The sound
source information calculated by CFD is imported into the
sound pressure calculation process. The prediction process
based on CFD/BEM is shown in Fig.9.
Flow field simulation(time domain)
Sound field simulation
(frequency domain)
Compressor steady flow field simulation
Compressor transient flow field simulation
Compressor dipole sound source (CGNS)
Sound source information import and data transfer
Acoustic boundary definition
Sound field calculation and
analysis
Figure 9. Noise prediction process
The calculation formula of compressor blade passing
frequency is shown below:
60
BPF
nZf (9)
The compressor blade passing frequency and its first two
order harmonics are 4921.7Hz、9843.5Hz and 14765.2Hz,
shown in Table 3.
Table 3. BPF and its harmonics
BPF 1st harmonic 2nd harmonic
Frequency(Hz) 4921.7 9843.5 14765.2
The compressor sound pressure level will be calculated by
the simulation method presented in this paper. In the process of
numerical calculation, the sound field is predicted by the
surface dipole noise model, because the contribution of the
dipole is much larger than the monopole and the quadrupole.
The sound pressure spectrum of all reference points are shown
in Fig.10. It can be found that the sound pressure spectrum
presents a typical characteristic of the impeller machinery
aerodynamic noise. The dominating source mechanisms of the
compressor aerodynamic noise were BPF and its harmonics,
just like the experiment results listed in previous literatures. The
measuring point 1 which is located near the compressor inlet
also has the largest total sound pressure level. The measuring
point that is closer to the inlet of the compressor has the greater
sound pressure level. Because the computational time and
computer hardware limits, the noise spectrum of numerical
calculation seems rougher.
Non-reflecting
Boundary
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0 2500 5000 7500 10000 12500 15000 17500 20000 22500
0
20
40
60
80
100
SP
L/d
B
f /Hz
P1
P2
P3
P4
P5
P6
P7
P8
P9
4829.1Hz9286.8Hz
13744.4Hz
Figure 10. Numerical simulation sound pressure level
The sound pressure distribution at inlet of turbocharger is
shown in the Fig.11. The pressure distribution of compressor
nozzle showed different patterns at each formant of Fig. 10.
(a) 995Hz
(b) 3096Hz
(c) BPF
(d) 1st harmonic
(e) 2nd harmonic
Figure 11. Pressure distribution of compressor nozzle
It can be found in Fig.11 that the sound pressure
distribution are significantly different at different frequencies,
which is decided by the sound wavelength especially in low
frequency. Compared with the wavelength, the size of inlet pipe
is smaller, and the sound wave diffraction phenomenon will
occur at orifice. The pipe diameter in this paper is 0.141m, so
the corresponding frequency which is equal to the acoustic
wavelength is as follows,
2432c
f Hz
(10)
In Eq. (10), 343 /c m s , 0.141m . In fig. 11 (a), the
sound wave propagate in the form of spherical wave. When the
frequency is higher than 2432Hz, the acoustic wavelength will
be smaller than orifice size, orifice acoustic diffraction
phenomenon gradually disappeared and sound wave reflection
phenomenon occurred at pipe orifice.
2. EXPERIMENTAL STUDY
2.1 Experiment facility For testing the validity of simulation method presented in
this paper, the turbocharger noise experiment bench was
designed and built, shown in Fig. 12. The gas provided by the
high-pressure air compressor will be burn fully in the burner.
The high temperature, high pressure gas obtained in the burner
would be used to simulate the diesel exhaust, and the gas is
leaded into the turbine and drive the turbine rotating. At the
same time, the coaxial compressor was driven to rotate by
turbine. There is a front exhaust value on the pipeline used to
adjust the amount of gas entering the turbine to control the
rotational speed of the turbocharger. The opening degree of the
electric control valve can be changed by the control device to
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change the gas intake of the turbine easily. The experimental
pressure ratio adjustment can be achieved by changing the
compressor outlet back-pressure through the butterfly regulating
value [3, 21]. Pressure, temperature and vibration sensors are
arranged in the turbine and compressor connecting pipe, the
operating parameters of the compressor are measured and then
used to guide the numerical calculation.
Figure 12. Experiment facility
Distribution details of the turbocharger and pipes used for
experimental measurements are shown in Fig 13. The
turbocharger is fixed on the bracket, turbine outlet is connected
with the exhaust muffler to reduce the exhaust noise,
compressor inlet is open to air directly.
Figure 13. Turbocharger detail diagram
The noise measuring points are distributed as shown in Fig
14(a). The turbocharger is simplified as a cube and its size is
0.4 0.4 0.4m m m . In Fig.14 (a), the negative X axis direction
was the air-inlet direction of the turbocharger. Measurement
points 1-5 were the middle points on each surface, and points 6-
9 were edge points respectively. To get the coordinates of each
monitoring point, we computed them according to the length
shown in Fig.14 (b) and Fig.14 (c). The distance of reference
points are shown as Eq.(10) and Eq. (11).
1 2 3 0.4L L L m (10)
1.0d m (11)
The other distance parameters in the measurement surface
are calculated by the following formula.
1
2
La d (12)
2
2
Lb d (13)
3c L d (14)
2
ch (15)
(a)
(b)
(c)
Figure 14. Measurement points distribution
2.2 Experimental results The sound pressure spectrum of each measurement point is
shown in Fig.15. It shows that the BPF and its harmonics
dominate the compressor aerodynamic noise. Its first two order
harmonic calculated by (9) are 4921.7Hz、 9843.5Hz and
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14765.2Hz, accordingly. The corresponding frequencies of the
experimental measurements are 4912.0Hz 、 9824.0Hz and
14736.0Hz. Two sets of data are compared in Table.4 and the
results are nearly same. The slight error might be the sensor
error or the instability of the compressor operation.
Table 4. Frequency comparison
BPF 1st harmonic 2nd harmonic
Theoretical
frequency(Hz) 4921.7 9843.5 14765.2
Experimental
frequency(Hz) 4912.0 9824.0 14736.0
error 0.20% 0.20% 0.20%
0.0 5.0x103
1.0x104
1.5x104
2.0x104
20
40
60
80
100
SP
L /dB
A
P1
(a) Measuring point1
(b) Nine measuring points
Figure 15. Experimental sound pressure level
Fig. 15 shows that the trend of all reference points is same.
The measuring point 1 which located at the compressor inlet
side has the largest sound pressure level. The measuring points
that are closer to the inlet of the compressor have the greater
sound pressure level.
2.3 Validity of calculation method All the information used in CFD and IBEM calculations
were got from the experiment measurement. The rotation speed
of experiment condition used in this paper is 36913 rpm. The
numerical calculation of centrifugal compressor aerodynamic
noise was completed with the pressure fluctuation data on the
rotor inlet surface and blade surface that got from flow field
analysis.
In Fig.16, three method result are plotted together, which
are traditional method (dots), CFD/BEM method (solid black
line) and experimental method (solid red line).
The sound pressure level of the BPF and its first two order
harmonic frequencies that are calculated with the pressure
fluctuation data of the blade surface is shown as the three dots.
The sound pressure level on the fundamental frequency and the
harmonic frequencies agree very well with the experiment
result. This method is much less time-consuming, in the
industrial design and the preliminary study of noise control, it
can play a very important role.
The fundamental frequency of experiment and calculation
by presented method in this paper are respectively 4912.96Hz
and 4829.12Hz, and the corresponding sound pressure value are
96.32dB and 96.54dB, indicating that the numerical calculation
result are predicted with sufficient accuracy. Table.5 show a
more detailed comparison. The errors are all calculated with
numerical calculation results and experimental results.
The results calculated by presented method agree well with
the experimental results, which are shown in Fig.16 and Tab. 5.
The trend of sound pressure curve is nearly envelop line of
experimental curve. The difference of peak value at blade
passing frequency is same. The error is not too much under 1st
harmonic frequency. With the calculating frequency is
increasing, the error of two method will be bigger.
0.0 5.0x103
1.0x104
1.5x104
2.0x104
20
40
60
80
100
SP
L /dB
f /Hz
tranditional simulation
continuous spectrum simulation
experimental measurement
Figure 16. Comparison of calculation and experimental results
Table 5 Results comparison
BPF 1st harmonic 2nd harmonic
Theoretical
frequency(Hz) 4921.7 9843.5 14765.2
Calculation
frequency(Hz) 4829.1 9286.8 13774.4
Experiment
frequency(Hz) 4912.0 9824.0 14736.0
0.0 5.0x103
1.0x104
1.5x104
2.0x104
40
50
60
70
80
90
100
SP
L/d
B
f /Hz
P1
P2
P3
P4
P5
P6
P7
P8
P9
4912Hz9824Hz
14736Hz
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Frequency
error 1.69% 5.47% 6.53%
Calculation
SPL(dB) 96.5 92.9 86.3
Experiment
SPL(dB) 96.3 93.6 80.5
SPL error 0.21% 0.75% 7.21%
3 CONCLUSION The coupling method combining CFD and IBEM in
compressor aerodynamic noise prediction is presented in this
paper. The experimental bench is built and the validity of the
method is tested.
(1) The calculation results for sound pressure in the whole
frequency band are agree very well with the experiment
result. The trend of curve is nearly same.
(2) The sound pressure near the inlet of turbocharger is higher
than other position. As the distance from the inlet
increasing, the sound pressure is smaller. Some devices like
intake muffler can be the effective way to control the
turbocharger noise.
(3) Comparing with the existing method, the simulation
frequency band expands from fixed BPF points to the
frequency range. More information such as fluid
characteristic, all band sound pressure and sound
distribution can be obtained in the same time, which can be
used for noise prediction and noise control.
ACKNOWLEDGMENTS The authors acknowledge the support for this research
work by Research Institute of Power Engineering Technology of
Harbin Engineering University.
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