acoustic modal analysis using cfd
TRANSCRIPT
Acoustic Modal Analysis using CFD M. Caraeni1, M. Oswald2
1 ANSYS Inc., Lebanon, NH 03766, USA, Email: [email protected]
2 ANSYS Germany GmbH, 64295 Darmstadt, Germany, Email: [email protected]
Abstract One of the most important issues in aeroacoustics design and development is the optimization of noise and vibration in both interior and exterior design processes. Especially the subjective comfort depends strongly on the interior noise. Besides the experimental investigations of the aeroacoustic phenomenon, numerical simulations have become more and more an effective tool to shorten the development cycle. This paper proposes a new approach based on a finite volume method for determining the resonance frequencies for enclosures. The current formulation requires as input the non-uniform mean flow obtained from a steady state solution together with prescribed boundary conditions. The method involves coupling the Linearized Navier-Stokes Equations with the Arnoldi algorithm. The Acoustic Modal Analysis, based on the iterative Implicitly Restarted Arnoldi method, offers a fast and efficient solver for large industrial eigenvalue problems. Using the data from this model, the natural acoustic modes of the system and the corresponding frequencies can be identified. These modes can resonate with interior acoustic source processes. The potential of the new method will be presented by means of several academic and industrial test cases ranging from thermo-acoustics to typical automotive and aerospace applications.
Introduction In many industrial applications there is the need to reduce
the acoustics related flow-field oscillations. Flows inside
enclosures are typical cases for resonance investigations.
Strong oscillatory phenomena can be found in the aerospace
industry, in the turbomachinery industry (combustion
chambers, etc.) and the automotive industry (car’s interior,
climate control ducts, etc.).
The Modal Analysis using CFD is a novel computational
tool, which is based on a Finite-Volume (FV) formulation. A
standard CFD simulation based on the compressible
Reynolds-Averaged Navier-Stokes equations (RANS)
provides the steady-state flow field with pressure, velocity
and temperature distributions. Depending on the steady state
results, the Modal Analysis computes the acoustic resonance
frequencies and the related acoustic (natural) modes in any
enclosure. Additionally, the model provides a stability
analysis of the computed modes. This paper presents the
theory of the Modal Analysis and a series of validation
cases.
Modal Analysis Theory The base equations of fluid mechanics (e.g. conservation of
mass, momentum and energy) are used to predict acoustic
modes and resonance frequencies. Only the mean flow
effects are taken into account to compute the acoustic
resonances.
First, the conservation of mass, momentum and energy are
expressed in differential form:
( )0=
∂∂+
∂∂
j
j
xu
tρρ
(1)
( ) ( )j
ij
ij
jii
xxp
xuu
tu
∂∂+
∂∂−=
∂∂+
∂∂ τρρ
(2)
( ) ( ) ( ) ( )Txu
xhu
te
j
iij
j
j ∇⋅∇+∂
∂=∂
∂+∂
∂ λτρρ (3)
where τij is the molecular stress tensor,
∂∂+
∂∂+
∂∂−=
i
i
i
j
k
kijij
x
u
x
u
x
u
2
1
32
δμτ (4)
Here, δij is the Kronecker delta function, μ is the molecular
viscosity, λ is the conductive heat diffusivity coefficient, cv
and cp are the specific heats at constant volume and constant
pressure, respectively,
21
1
2
22ii
vupu
Tce +−
=+=ργ
(5)
is the total energy per unit mass and
21
2iupp
eh +−
=+=ργ
γρ
(6)
is the total enthalpy per unit mass and γ is the ratio of the
specific heats.
Second, the linearized form of the conservation of mass,
momentum and energy can be achieved by superimposing
small perturbations on the mean flow. To model the
acoustics, this system of linearized Navier-Stokes equations
with appropriate boundary conditions is solved. These
equations can be written as:
00
0
0 =∂
′∂+∂∂′+
∂′∂+
∂∂′+
∂′∂
jj
j
j
j
j
j
xp
xu
xu
xu
tp ρρρ (7)
=∂∂′
−∂
′∂+∂∂′+
∂′∂+
∂′∂
iij
ij
j
ij
i
xp
xp
xu
uxu
ut
u 0
02
0
0
0
1
ρρ
ρ
∂∂+
∂∂+
∂∂′
−∂
′∂+∂
′∂+∂
′∂3
30
2
20
1
10
02
3
3
2
2
1
1
0
1
xxxxxx
iiiiii τττρρτττ
ρ (8)
( )10
0
0
0 −=∂∂′+
∂′∂+
∂∂′+
∂′∂+
∂′∂ γγγ
j
j
j
j
j
j
j
j
xu
pxu
pxp
uxp
utp
( ) ( ) ( )∂
∂′−∂
′∂−′∇⋅∇+∂′∂+
∂′∂
j
iji
j
iji
j
iji
j
iji
xu
xuT
x
u
x
u 0
0
00 ττλττ
(9)
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The mean flow conditions are available
CFD simulation of the full Navier-Stoke
linearized form of the Navier-Stokes equ
compute the eigenvalues/eigenvectors of
coupled system of the Navier-Stokes eq
form can be written as:
0)(Re =+∂∂
Qst
Q
Where Q = (ρ, ρu, ρv, ρw, ρΕ) are the c
variables. With W = (p, u, v, w, T) as primi
can write:
0)(Re =+∂
∂∂∂
Wst
W
W
Q
Linearization presumes that the steady
averaged) solution W0 = (p0, u0, v0, w0, T0
with small perturbations of the primitive v
u´, v´, w´, T´). Fourier decomposition can
perturbation, when we consider a time p
solution. Equation (11) can be reformulated
( ) ( ) ( ) ( ) (ixWxtxWxtW +=+= ωexp,W, 0'
0
And after mathematical manipulations:
( ) ( ) ( ) ( ) 0'*Re'**
0 =∂
∂+∂∂
xWW
WsxW
W
Qiω
The Jacobians W
Q
∂∂
and ( )
W
Ws
∂∂ 0Re
linearizations of the discretized flow equati
With λ = -iω, this system of equations can b
( )[ ] [ ] 0=+− XAXBλ
[ ] XX λ=
where [ ] ( )W
WsA
∂∂
= 0Re, [ ] [ ] [ ]AB 1−= ,
( )xWX '= is the solution of the eigenvalu
the eigenvector for the complex eigenvalu
Analysis considers the coupled system o
including continuity, momentum, ener
transport. The proper acoustic response
included in the Modal Analysis. For furth
refer to [5].
The iterative Implicitly Restarted Arnoldi
based on ARPACK package is used to solv
problem (15). IRAM is a robust and efficie
numerical solution of a generalized eige
This model allows solving only for
eigenvalues and the corresponding eigenv
on the range of interest of an engineering
implementation in FLUENT® uses a s
which was formulated as a standard eig
The eigenvalue λ, λ= -iω, and the angul
both complex numbers. The sign of the
eigenvalue gives the stability of the corr
Reformulating W´:
from a precursor
es equations. The
uations is used to
the system. The
quations in vector
(10)
coupled conserved
itive variables, we
(11)
y-state (or time-
0) is superimposed
ariables W´ = (p´,
be applied on the
periodic perturbed
d into:
) ( )xWt ′⋅ω (12)
0 (13)
are the direct
ions.
be written as:
(14)
(15)
, [ ]W
QB
∂∂= and
ues problem. W´ is
ue λ = -iω. Modal
of equations (15),
rgy and species
of boundaries is
her details, please
i Method (IRAM)
ve the eigenvalues
ent method for the
envalues problem.
a small set of
vectors, depending
g application. The
hift-mode driver,
genvalue problem.
ar velocity ω are
e real part of the
responding mode.
( ) ( ) ( ) =′= xWtixt ωexp,W'
( ) ( ) ( )xWtti ri'expexp ⋅−⋅− λλ
one can show that the most un
the largest negative real part
real part indicates exponential
mode. The imaginary part
(frequency for mode’s oscillati
improves the convergence f
frequency spectrum. We can sh
scalar, λ0, and reformulate (15)
[ ] XX λ′=
with [ ] [ ] [ ] IAB 01 λ−= −
and
corresponding to eigenvalue λeigenvalues of this new s
transformed back to the eigen
Then, the frequencies of the
using:
( )πλλ
πλν
22
0iii +′==
Numerical results Box resonator
Simple resonator geometries ar
the fact that we can estimate
given temperature distribution
We consider two resonator ca
and the open resonator. The M
only the resonance frequencies
The domain of the closed box
length of 1m. All six side face
with constant temperature of 2
rest with the same temperature
the velocity perturbation is ma
at the two opposite walls. Henc
mode is equal to two times the
frequency for a box with afores
Hzc
f 1.1732
1.346 ===λ
The modal analysis calculates
(172.8 Hz). Figure 1 shows
frequencies of 173
Figure 1: Normalized pressurresonator (173 Hz and 345 Hz
(16)
nstable mode is represented by
eigenvalues (λr). A negative
ly increasing amplitude of the
indicates the angular speed
ion). The shift mode algorithm
for a desired range of the
hift the range of interest with a
) as:
(17)
d ( )xWX ′= , the eigenvector
0λλλ −=′ . After solving the
ystem, the eigenvalues are
nvalues of the original system.
original system are obtained
(18)
re good validation cases due to
the resonance frequencies for
ns and geometry dimensions.
ases: the closed box resonator
Modal Analysis calculates not
s, but also the acoustic modes.
resonator is a cube with a side
s are set to be wall boundaries
298 K. The box contains air at
e. For the first acoustic mode,
aximal in the middle and zero
ce, the wave length of the first
e box size. The first theoretical
said dimensions is therefore:
(19)
a frequency of about 173 Hz
the acoustic modes for the
Hz and 345 Hz.
re fluctuations for closed box )
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A similar test case with one open side was
Modal Analysis. The open side was tre
outlet with static pressure 1 bar. The first
the mode for which the velocity perturbat
the open side. The first theoretical frequen
the foresaid dimensions is:
Hzc
f 5.864
1.346 ≅==λ
The frequencies calculated with the
algorithm match the theoretical value
frequency obtained with modal analysis: 8
shows the acoustic modes for the frequenc
354 Hz.
Figure 2: Normalized pressure fluctuationresonator (86 Hz and 354 Hz)
Double diaphragm
This is another case, where the coupling o
with the instantaneous flow field is imp
diaphragm is placed inside a circular duct w
0.05 m. The distance between the two diaph
1D. Turbulent eddies detached from the
impact the second diaphragm where stro
fluctuations are generated.
At the inlet the total pressure profile – co
Reynolds number of 15,000 - and the turbu
and ε, obtained from a previous LES run
The rotational periodic/symmetric geomet
good test case to investigate the effect
periodic boundary conditions on the moda
Analysis was performed on a full geome
cells and on a quadrant of the pipe with 7
symmetry as well as periodic boundary
predicted resonance frequencies and aco
identical (see table 1), hence Modal Anal
with periodic and symmetry conditions,
necessary simulation time. A comparison
based solver with the density-based s
identical results, which extends the ran
density-based solver is proper for all flo
incompressible to highly compressible
geometry case with 280,000 cells correspo
the resolution of the quadrant geometry w
count. The comparison between measured
and discrete acoustic modes is shown in F
the modal analysis will not give any i
s conducted using
ated as pressure-
acoustic mode is
tion is maximal at
ncy for a box with
(20)
Modal Analysis
very well (first
86.4 Hz). Figure 2
cies of 86 Hz and
ns for open box
of Modal Analysis
portant. A double
with a diameter of
hragms is equal to
e first diaphragm
ong wall pressure
orresponding to a
ulent profiles for k
[6], were applied.
try and flow is a
of symmetry and
al analysis. Modal
etry with 280,000
77,000 cells using
y conditions. The
oustic modes are
lysis can be used
which decreases
n of the pressure-
olver gives also
nge of use. The
ow regimes from
cases. The full
onds to four-times
with the same cell
frequency spectra
igure 5. Note that
nformation about
amplitude, hence no dB valu
modal analysis is presented at
3.
Figure 3: Comparison of m
experimental data at micro1 (be
(behind 2nd diaphragm)
Data 360°
PBNS
360°
DBN
336 Hz 353 Hz 353 H
553 Hz - -
805 Hz 747 Hz 747 H
1108 Hz 1055 Hz 1055
Table 1: Measured resonanc
computed frequencies for full g
(PBNS) and density-based solver
(periodic and symmetri
Figure 4 shows the unstable mo
1055 Hz.
Figure 4: Normalized pressdiaphragm
Combustion chamber G
Identification of acoustic eigen
obligatory prerequisite of co
[7]. GE LM 6000 is a swirl stab
combustor. A steady-state simu
incoming flow velocity of 150
and a static pressure of 517,10
The medium is a mixture con
H2, OH, O, O2, CO, CO2 and
ues or can be predicted. The
an arbitrary dB value in figure
ost unstable modes with the
etween diaphragms) and micro2
°
NS
90° per.
PBNS
90° sym.
PBNS
Hz 353 Hz 353 Hz
- -
Hz 747 Hz 747 Hz
5 Hz 1056 Hz 1055 Hz
e frequencies compared with
geometry (pressure-based solver
r (DBNS)) and quarter geometry
ic boundary condition)
ode at 353 Hz, 747 Hz and
sure fluctuations for double
GE LM 6000
nmodes of the combustor is an
ombustion instability research
bilized partially-premixed fuel
ulation was conducted with an
0 m/s at temperature of 617 K
07 Pa on a 250,000 cells mesh.
ntaining CH3, N2, HO2, H2O,
d CH4. Turbulence was solved
NAG/DAGA 2009 - Rotterdam
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with the realizable k-ε turbulence model [
the modal analysis are summarized in table
Mode Frequ
First longitudinal 1L
Second longitudinal 2L
First tangential 1T
Second tangential 2T
First complex 1C
Second complex 2C
Table 2: Frequency and mode description
The lowest frequencies are acoustically d
sensitive to the effect of the combustion p
5 shows the first complex eigenmode at 346
Figure 5: Acoustic resonance mode at frequ
A full unsteady simulation with Large
(LES) was also performed. Fast Fourier Tr
been used for spectral analysis. To
frequencies, the LES has to run for long flo
required resolution of the frequency spe
frequency range the modal analysis has a
transient methods. Figure 6 shows the insta
magnitude in the symmetry plane of
chamber. Frequencies less than 7000 Hz a
the modal analysis model in figure 7.
Figure 6: Instantaneous vorticity magnitudthe symmetry plane of combustion chambesimulation
Figure 7: Discrete frequency spectrum resuusing the CAA approach compared with MA
[8]. The results of
2.
uency [Hz]
80
180
980
1973
3462
4675
n of combustor
driven and are not
process [9]. Figure
62 Hz.
uency 3427 Hz
e-Eddy-Simulation
ransformation has
predict the low
ow time to get the
ectra. In the low
an advantage over
antaneous vorticity
the combustion
are compared with
e distribution in r from unsteady
ults as computed A results
Summary A fast finite-volume based m
computing the resonance frequ
any complex enclosures is pres
This fast and accurate numeri
non-uniform flow field obtaine
computation. Based on th
equations with appropriate
generalized eigenvalue probl
solved using IRAM.
The Modal Analysis method b
orders of magnitude more
approach, of computing the
direct unsteady simulation.
References [1] Wind-tunnel experiments
cavities at subsonic and tr
Technical Report 3438, A
Reports and Memoranda,
[2] On the tomes and pressur
flow over rectangular cav
P.J.W., Fluid Mechanics, V
[3] Modelling and predictio
amplitude and frequency
McCotter F., Technical Re
[4] Estimation of possible exc
shallow rectangular cavitie
AIAA Journal, Vol. 11, pp
[5] Efficient acoustic modal an
Caraeni M. et al, AIAA-20
[6] Simulation of Aeroacousti
Control Systems, Mathey F
AIAA-2006-2493,2006
[7] Prediction and Control of C
Industrial Gas Turbines, K
Thermal Engineering 24, 1
[8] A New k-ε Eddy-Viscosity
Number Turbulent Flows -
Validation. Shih T.H. et al
24(3):227-238, 1995.
[9] Low-frequency combustio
vortices. Pointsot T. et al,
International de l’Energy,
method, based on IRAM, for
uencies and acoustic modes of
sented.
ical method uses as input the
ed from a previous steady-state
he linearized Navier-Stokes
e boundary conditions a
lem is formulated, which is
based on IRAM proves to be
efficient than the classical
resonance frequencies from
on the flow over rectangular
ransonic speeds. Rossiter J.E.,
Aeronautical Research Council
1964
re oscillations induced by the
vities. Tam C.K.W. and Block
Vol.89 pp. 373-399, 1978
n of weapons bay acoustic
y. Cain A.B., W.W. Bower,
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citation frequencies for
es. Covert E.E., Bilanin A.J.,
p 347-351, 1973
nalysis for industrial CFD.
009-1332, 2009
ic Sources in Aircraft Climate
F, Morin O., Caruelle B.,
Combustion Instabilities in
Kelsall G., Troger C., Applied
1571-1582, 2004.
y Model for High Reynolds
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on instabilities driven by large
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