# Analytic Formulation for the Sound Absorption of a Panel Absorber under the Effects of Microperforation, Air Pumping, Linear Vibration and Nonlinear Vibration

Authors: Y. Y. Lee
Journal: Abstract and Applied Analysis
 (2014)

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## Abstract

This study includes the first work about the absorption of a panel absorber under the effects of microperforation, air pumping, and linear and nonlinear vibrations. In practice, thin perforated panel absorber is backed by a flexible wall to enhance the acoustic performance within the room. The panel is easily excited to vibrate nonlinearly and the wall can vibrate linearly. However, the assumptions of linear panel vibration and no wall vibration are adopted in many research works. The development of the absorption formula is based on the classical approach and the electroacoustic analogy, in which the impedances of microperforation, air pumping, and linear and nonlinear vibrations are in parallel and connected to that of the air cavity in series. Unlike those finite element, numerical integration, and multiscale solution methods and so forth, the analytic formula to calculate the absorption of a panel absorber does not require heavy computation effort and is suitable for engineering calculation purpose. The theoretical result obtained from the proposed method shows reasonable agreement with that from a previous numerical integration method. It can be concluded that the overall absorption bandwidth of a panel absorber with an appropriate configuration can be optimized and widened by making use of the positive effects of microperforation, air pumping, and panel vibration.


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## Body

## 1. Introduction

Numerous studies of structural-acoustic interaction have been carried out in recent decades (e.g., [1–6]). Particularly, the topics of microperforated panel and panel absorber have attracted the interest of many researchers. It is because (1) microperforated panel and panel absorber can be made of any durable materials, (2) their maintenance is relatively simple, and (3) microperforated panel requires small space to achieve high sound absorption when compared with typical foam or porous materials. Acoustic theories for these two treatments were developed by Mulholland and Parbrook [7], Ford and McCormick [8], and Maa [9, 10]. According to the assumptions of the previous studies, the wall behind a panel absorber was considered as rigid panel (i.e., no vibration) and the panel absorber was considered to vibrate linearly (in fact, thin panels are easy to vibrate nonlinearly). Although many linear structural-acoustic or nonlinear structural vibration problems had been solved (e.g. [11–17]), very limited studies considered the nonlinear vibration effect on the sound absorption performance of a panel absorber. In fact, it is more appropriate to employ nonlinear approach to analyze the vibration of a thin panel. There are five of those limited nonlinear structural-acoustic research works [18–22], which focused on the natural frequencies of nonlinear structural-acoustic systems, and the sound absorption, radiation, and transmission of nonlinear flat/curved panels. These works are relevant to the nonlinear structural-acoustic problem handled in this paper, but the researchers adopted the solution methods which required heavy computational efforts (e.g., finite element method, numerical integration method, and harmonic balance method). Other solution methods for large amplitude structural vibrations and nonlinear oscillations (e.g., the method of multiple scales, the method of normal forms, the method of Shaw and Pierre, and the method of King and Vakakis [23–27]) also require relatively tedious solution implementation and heavy computational efforts. In [28], the simple and straightforward electroacoustic analogy was adopted for modelling of the sound absorption of a panel absorber. Besides, the air pumping effect (or Helmholtz resonance effect) has been mentioned in many textbooks and articles (e.g., [29]), but it has not been incorporated into the research problem of nonlinear panel absorber. In this paper, it focuses on the development of the analytic absorption formula of a panel absorber which considers the four effects (i.e., microperforation, air pumping, and linear and nonlinear vibrations).


## 2. Analytic Formulation

### 2.1. Nonlinear Panel Vibration and Liner Wall Vibration

Figure1 shows the proposed panel absorber subject to the effects of microperforation, air pumping, and linear and nonlinear vibrations. Firstly, the impedances of the nonlinear panel and linear wall are derived in this subsection. According to the formulation of Chu and Herrmann [30], the governing equation for the nonlinear vibration of a rectangular panel subject to uniformly distributed harmonic excitation can be expressed in the following form (see Appendix A for more):
(1)
ρ
d
2
ε
d
τ
2
+
ρ
ω
o
2
ε
+
β
ε
3
+
F
(
τ
)
=
0
,
whereF
(
τ
)
=
F
o
,
m
n
sin
(
ω
τ
)
= modal harmonic excitation,
F
o
,
m
n
=
F
o
Λ
m
n
=
λ
ρ
t
g
Λ
m
n
= modal excitation magnitude,
F
o
=
λ
ρ
t
g
= physical excitation magnitude,
g
= gravity acceleration (9.81 ms−2),
τ
= time,
λ
= dimensionless excitation parameter,
(2)
Λ
m
n
=
(
∫
0
b
∫
0
a
sin
(
m
π
x
/
a
)
sin
(
n
π
y
/
b
)
d
x
d
y
)
∫
0
b
∫
0
a
[
sin
(
m
π
x
/
a
)
sin
(
n
π
y
/
b
)
]
2
d
x
d
y
=
modal
coefficient
,
ω
= excitation frequency,
ω
o
= linear resonant frequency of the (m
,
n) mode,
m
,
n
= structural mode numbers,
(3)
β
=
E
t
12
(
1
-
ν
2
)
a
4
3
π
4
2
β
×
[
1
2
m
2
(
m
2
+
ν
n
2
r
2
)
(
-
3
2
+
ν
n
2
r
2
m
2
)
-
3
4
n
2
r
2
(
n
2
r
2
+
ν
m
2
)
aaaa
β
aa
-
3
4
m
2
(
m
2
+
ν
n
2
r
2
)
aaa
β
aaa
+
1
2
n
2
r
2
(
n
2
r
2
+
ν
m
2
)
(
-
3
2
+
ν
m
2
n
2
r
2
)
aaaa
β
aa
1
2
m
2
(
m
2
+
ν
n
2
r
2
)
(
-
3
2
+
ν
n
2
r
2
m
2
)
-
3
4
n
2
r
2
(
n
2
r
2
+
ν
m
2
)
]
β
=
nonlinear
stiffness
coefficient
,
r
=
a
/
b is the aspect ratio; E is Young’s modulus; ρ is the surface density; ν is Poisson’s ratio; and t, a, and b are the thickness, length, and width.Consider the approximation of ε
=
A
cos
⁡
(
ω
τ
) in (1). Then
(4)
3
4
β
A
3
+
ρ
(
ω
o
2
-
ω
2
)
A
+
F
o
,
m
n
=
0
,
⇒
(5)
A
3
+
4
3
β
ρ
(
ω
o
2
-
ω
2
)
A
+
4
3
β
F
o
,
m
n
=
0
,
where A
= modal vibration amplitude.Figure 1
A panel absorber subject to the effects of microperforation, air pumping, and linear and nonlinear vibrations.For simplicity, letp
=
(
4
/
3
β
)
ρ
(
ω
o
2
-
ω
2
)
,
q
=
(
4
/
3
β
)
F
o
,
m
n, and A
=
B
-
(
p
/
3
B
) (i.e., Vieta’s substitution [31]). Equation (5) can be rewritten as
(6)
B
3
+
q
-
p
3
27
B
3
=
0
,
⇒
(7)
B
6
+
q
B
3
-
p
3
27
=
0
.
If B
3 is considered as an independent unknown, (7) is a “modified” quadratic equation. Then, the analytic formulas for the cubic solutions are given below:(8a)
A
1
=
-
1
3
1
2
(
Θ
+
Ω
)
3
-
1
3
1
2
(
Θ
-
Ω
)
3
,
(8b)
A
2
=
1
+
j
3
6
1
2
(
Θ
+
Ω
)
3
+
1
-
j
3
6
1
2
(
Θ
-
Ω
)
3
,
(8c)
A
3
=
1
-
j
3
6
1
2
(
Θ
+
Ω
)
3
+
1
+
j
3
6
1
2
(
Θ
-
Ω
)
3
,where Θ
=
(
27
q
)
2
+
4
(
3
p
)
3, Ω
=
27
q.In the next step, the nonlinear stiffness can be defined as(
3
/
4
)
β
A
2 and overall panel stiffness is ρ
ω
o
2
+
(
3
/
4
)
β
A
2. The panel impedance of the (m
,
n) mode is given by
(9)
Z
P
,
m
n
=
F
o
,
m
n
V
P
,
m
n
=
2
ρ
ξ
ω
ω
N
+
j
[
ρ
(
ω
2
-
ω
o
2
)
-
(
3
/
4
)
β
A
2
]
ω
,
where j
=
-
1
= complex number; ξ is the panel damping ratio. V
P
,
m
n is the modal panel velocity. Note that ω
N is the nonlinear peak frequency, instead of the linear natural frequency, ω
o in [32] (see Appendix B for the derivation of ω
N). When it is the case of small amplitude vibration or linear vibration, ω
N is equal to ω
o.Consider the overall panel velocity contributed from the modal velocities and find the overall panel impedance:(10)
V
P
=
∑
m
M
∑
n
N
F
o
Λ
m
n
Λ
m
n
′
Z
P
,
m
n
,
⇒
(11)
Z
P
=
F
o
V
P
=
(
∑
m
M
∑
n
N
Λ
m
n
Λ
m
n
′
Z
P
,
m
n
)
-
1
,
where Λ
m
n
′
=
(
∫
0
b
∫
0
a
sin
(
m
π
x
/
a
)
sin
(
n
π
y
/
b
)
d
x
d
y
)
/
a
b. According to [33], the sound absorption of two linearly vibrating plates with different boundary conditions was very close. It was concluded that the boundary condition would not affect the sound absorption significantly. That is why only one boundary condition case is considered here.Consider the linear case (or small amplitude case) in the model representing the panel vibration and the corresponding modal and overall panel impedances (i.e., (9), (11)). It is noted that, for the linear vibration, the fundamental harmonic balance can lead to the exact solution (no higher harmonic terms are required). Hence the modal and overall wall impedances are given below:
(12)
Z
W
,
m
n
=
2
ρ
W
ξ
W
ω
ω
W
+
j
[
ρ
(
ω
2
-
ω
W
2
)
]
ω
,
(13)
Z
W
=
(
∑
m
M
∑
n
N
Λ
m
n
Λ
m
n
′
Z
W
,
m
n
)
-
1
,
where ξ
W
,
ρ
W, and ω
W are the wall damping factor, density, and natural frequency


### 2.2. Air Pumping (Helmholtz Resonance)

In Figure1, the impedance of the air pumping along the tube mounted on the panel absorber is obtained here. The differential equation for the air mass pumping in/out along the tube is given by [29]
(14)
ρ
a
L
′
d
2
Λ
d
τ
2
+
(
R
r
+
R
w
)
S
d
Λ
d
τ
+
P
(
τ
)
=
0
,
where Λ
= air mass displacement, P
(
τ
)
= acoustic pressure excitation, R
r
=
ρ
a
c
a
k
2
S
2
/
4
π
= damping due to radiation resistance, R
w
=
2
ρ
a
L
′
S
α
w
= damping due to thermoviscous resistance, L
′
=
L
+
1.4
a
t
= effective tube length, α
w
=
(
1
/
a
t
c
a
)
(
η
ω
/
2
ρ
a
)
0.5
(
1
+
(
γ
/
Pr
)
)
= absorption coefficient for wall losses, and ρ
a is the air density; L
′ is the effective length of the tube with unflanged outer end; k is the wave number; L is the tube length; a
t is the radius of the tube; S is the cross section area of the tube; η is the air viscosity; γ is the ratio of specific heat; Pr is Prandtl number.Similar to the overall panel impedance in (9), the impedance of air pumping along the tube is given below:
(15)
Z
H
′
=
(
(
R
r
+
R
w
)
/
S
)
ω
+
j
ρ
a
L
′
ω
2
ω
.
Using (15), the air mass velocity is given by
(16)
Z
H
′
=
P
o
V
H
′
⟹
V
H
′
=
P
o
Z
H
′
,
where P
o = acoustic pressure magnitude.Consider the average velocity over the panel surface(17)
V
H
=
V
H
′
σ
H
,
where σ
H
= the ratio of tube area to panel area.Then the overall impedance of air pumping is obtained by substituting (17) into (16):
(18)
Z
H
=
Z
H
′
σ
H
.


### 2.3. Microperforation

In Figure1, the impedance of the microholes over the panel surface is obtained here. According to [9, 10], the real and imaginary parts of the acoustic impedance of a microhole are given below:(19a)
Z
M
,
R
′
=
ρ
a
c
a
(
0.147
t
d
2
)
(
9
+
100
d
2
f
32
+
1.768
f
d
2
t
)
,
(19b)
Z
M
,
I
′
=
ρ
a
c
a
1.847
f
t
(
1
+
1
9
+
50
d
2
f
+
0.85
d
t
)
,where Z
M
′
=
Z
M
,
R
′
+
j
Z
M
,
I
′
= the impedance of a microhole, f is frequency, t is panel thickness, and d is the perforation diameter. ρ
a and c
a are air density and sound speed.Then, the overall impedance of all microholes over the panel is given by(20)
Z
M
=
Z
M
′
σ
,
where σ is the perforation ratio.


### 2.4. Air Cavity

In Figure1, the impedance of the air cavity is obtained here. The acoustic velocity potential within a rectangular cavity is given by the following homogeneous wave equation [1]:
(21)
∇
2
ϕ
-
1
c
a
2
∂
2
ϕ
∂
τ
2
=
0
,
where ϕ is the velocity potential function.The air particle velocities in thex, y, and z directions and pressures within the air cavity can be given by ∂
ϕ
/
∂
x
,
∂
ϕ
/
∂
y
,
∂
ϕ
/
∂
z, and -
ρ
a
(
∂
ϕ
/
∂
τ
), respectively.The boundary conditions of the rectangular cavity to be satisfied are(22a)
∂
ϕ
∂
x
|
x
=
0
=
∂
ϕ
∂
x
|
x
=
a
=
0
;
(22b)
∂
ϕ
∂
y
|
y
=
0
=
∂
ϕ
∂
y
|
y
=
b
=
0
,
(22c)
∂
ϕ
∂
z
|
z
=
0
=
0
;
(22d)
∂
ϕ
∂
z
|
z
=
-
D
=
V
D
,where a and b are the length and width of the rectangular cavity or the panel and V
D is the average velocity at z
=
D
= cavity depth. Note that the cavity impedance of no wall vibration is derived here and used into the sound absorption formulation in the next subsection which can consider both the panel and wall vibration effects and is derived using the electroacoustic analogy.By applying the boundary conditions in (22a) and (22b), the solution of (21) can be expressed as
(23)
ϕ
=
∑
u
=
0
U
∑
w
=
0
W
[
L
u
w
cosh
⁡
(
μ
u
w
z
)
+
N
u
w
sinh
⁡
(
μ
u
w
z
)
]
×
cos
⁡
(
u
π
x
a
)
cos
⁡
(
w
π
y
b
)
e
i
ω
τ
,
where μ
u
w
=
(
(
u
π
/
a
)
2
+
(
w
π
/
b
)
2
)
-
(
ω
/
c
a
)
2, u and w are the acoustic mode numbers, U and W are the numbers of acoustic modes used in the x and y directions, and L
u
w and N
u
w are coefficients to be determined in the following step.Substituting (23) into (22c) and (22d) gives(24a)
∂
ϕ
∂
z
|
z
=
0
=
0
⟹
N
u
w
=
0
,
(24b)
∂
ϕ
∂
z
|
z
=
D
=
V
D
e
i
ω
τ
⟹
L
u
w
=
-
∫
0
a
∫
0
b
V
D
cos
⁡
(
u
π
x
/
a
)
cos
⁡
(
w
π
y
/
b
)
d
x
d
y
κ
u
w
μ
u
w
sinh
⁡
(
μ
u
w
D
)
,where κ
u
w
=
∫
0
a
∫
0
b
cos
⁡
(
u
π
x
/
a
)
2
cos
⁡
(
w
π
y
/
b
)
2
d
x
d
y.By inputting (24a) and (24b) into (23), the pressure at z
=
D is obtained and given below:
(25)
F
D
=
∑
u
=
0
U
∑
w
=
0
W
[
j
ρ
a
ω
coth
⁡
(
μ
u
w
D
)
κ
u
w
μ
u
w
a
a
a
a
a
a
a
a
a
×
coth
⁡
(
μ
u
w
D
)
κ
u
w
μ
u
w
∫
0
a
∫
0
b
V
D
cos
⁡
(
u
π
x
a
)
cos
⁡
(
w
π
y
b
)
d
x
d
y
]
×
cos
⁡
(
u
π
x
a
)
cos
⁡
(
w
π
y
b
)
.
The average pressure force at z
=
D is then given by taking integration over the panel area
(26)
F
¯
D
=
∫
0
a
∫
0
b
F
D
cos
⁡
(
u
π
x
/
a
)
cos
⁡
(
w
π
y
/
b
)
d
x
d
y
a
b
=
V
D
j
ρ
a
ω
∑
u
=
0
U
∑
w
=
0
W
[
κ
u
w
′
κ
u
w
coth
⁡
(
μ
u
w
D
)
μ
u
w
]
,
where κ
u
w
′
=
(
∫
0
a
∫
0
b
cos
⁡
(
u
π
x
/
a
)
cos
⁡
(
w
π
y
/
b
)
d
x
d
y
)
2
/
a
b.Finally, the impedance of the air cavity is given by(27)
Z
cav
=
F
¯
D
V
D
=
j
ρ
a
ω
∑
u
=
0
U
∑
w
=
0
W
[
κ
u
w
′
κ
u
w
coth
⁡
(
μ
u
w
D
)
μ
u
w
]
.
Note that since even pressure distribution is considered, then u
,
w
=
0,2
,
4
,
…. If a and b are less than 0.3 m, then the frequencies of the fundamental resonances parallel to the cavity length or width are higher than 1000 Hz (note that 1000 Hz is not within the frequency range concerned in this study). Then, in this case, only the mode numbers, u
=
0 and w
=
0, are considered. The impedance can be approximated by
(28)
Z
cav
≈
-
j
ρ
a
ω
cot
(
ω
c
a
D
)
.


### 2.5. Electroacoustic Analogy

According to [34], the acoustic impedance of a double panel absorber can be analogous to that of the electrical circuit. The acoustic impedance is given below:
(29)
Z
dou
=
Z
p
,
1
+
Z
cav
,
1
+
(
Z
cav
,
1
)
2
Z
p
,
2
+
Z
cav
,
1
+
Z
cav
,
2
,
where Z
p
,
1 and Z
p
,
2
= acoustic impedance of the 1st and 2nd panels; Z
cav
,
1 and Z
cav
,
2
= acoustic impedance of the 1st and 2nd cavities.If the impedance of the 2nd cavity is set to zero, that is, equivalent to the case of a panel absorber backed by a flexible wall, the overall impedance in (29) is rewritten as
(30)
Z
o
=
Z
com
+
Z
cav
+
(
Z
cav
)
2
Z
W
+
Z
cav
,
where Z
com
=
(
Z
M
Z
P
Z
H
)
/
(
Z
M
Z
P
+
Z
P
Z
H
+
Z
H
Z
M
)
= combined impedance. Z
M
= impedance of the microperforation; Z
P
= acoustic impedance of the panel absorber; Z
H
= impedance of the air pumping; Z
W
= impedance of the wall.If the wall is perfectly rigid (i.e., no vibration), the natural frequency of wallω
W in (12)→
∞. Hence, Z
W
,
m
n, Z
W
→
∞ and (
Z
cav
)
2
/
(
Z
W
+
Z
cav
)
≈
0. Equation (30) can be rewritten as
(31)
Z
o
=
Z
com
+
Z
cav
.
Then the absorption coefficient of the absorber α
o for normal incidence can be calculated by the well-known formula (see [29]):
(32)
α
o
=
4
Re
(
Z
o
)
(
1
+
Re
(
Z
o
)
)
2
+
(
Im
⁡
(
Z
o
)
)
2
.


## 2.1. Nonlinear Panel Vibration and Liner Wall Vibration

Figure1 shows the proposed panel absorber subject to the effects of microperforation, air pumping, and linear and nonlinear vibrations. Firstly, the impedances of the nonlinear panel and linear wall are derived in this subsection. According to the formulation of Chu and Herrmann [30], the governing equation for the nonlinear vibration of a rectangular panel subject to uniformly distributed harmonic excitation can be expressed in the following form (see Appendix A for more):
(1)
ρ
d
2
ε
d
τ
2
+
ρ
ω
o
2
ε
+
β
ε
3
+
F
(
τ
)
=
0
,
whereF
(
τ
)
=
F
o
,
m
n
sin
(
ω
τ
)
= modal harmonic excitation,
F
o
,
m
n
=
F
o
Λ
m
n
=
λ
ρ
t
g
Λ
m
n
= modal excitation magnitude,
F
o
=
λ
ρ
t
g
= physical excitation magnitude,
g
= gravity acceleration (9.81 ms−2),
τ
= time,
λ
= dimensionless excitation parameter,
(2)
Λ
m
n
=
(
∫
0
b
∫
0
a
sin
(
m
π
x
/
a
)
sin
(
n
π
y
/
b
)
d
x
d
y
)
∫
0
b
∫
0
a
[
sin
(
m
π
x
/
a
)
sin
(
n
π
y
/
b
)
]
2
d
x
d
y
=
modal
coefficient
,
ω
= excitation frequency,
ω
o
= linear resonant frequency of the (m
,
n) mode,
m
,
n
= structural mode numbers,
(3)
β
=
E
t
12
(
1
-
ν
2
)
a
4
3
π
4
2
β
×
[
1
2
m
2
(
m
2
+
ν
n
2
r
2
)
(
-
3
2
+
ν
n
2
r
2
m
2
)
-
3
4
n
2
r
2
(
n
2
r
2
+
ν
m
2
)
aaaa
β
aa
-
3
4
m
2
(
m
2
+
ν
n
2
r
2
)
aaa
β
aaa
+
1
2
n
2
r
2
(
n
2
r
2
+
ν
m
2
)
(
-
3
2
+
ν
m
2
n
2
r
2
)
aaaa
β
aa
1
2
m
2
(
m
2
+
ν
n
2
r
2
)
(
-
3
2
+
ν
n
2
r
2
m
2
)
-
3
4
n
2
r
2
(
n
2
r
2
+
ν
m
2
)
]
β
=
nonlinear
stiffness
coefficient
,
r
=
a
/
b is the aspect ratio; E is Young’s modulus; ρ is the surface density; ν is Poisson’s ratio; and t, a, and b are the thickness, length, and width.Consider the approximation of ε
=
A
cos
⁡
(
ω
τ
) in (1). Then
(4)
3
4
β
A
3
+
ρ
(
ω
o
2
-
ω
2
)
A
+
F
o
,
m
n
=
0
,
⇒
(5)
A
3
+
4
3
β
ρ
(
ω
o
2
-
ω
2
)
A
+
4
3
β
F
o
,
m
n
=
0
,
where A
= modal vibration amplitude.Figure 1
A panel absorber subject to the effects of microperforation, air pumping, and linear and nonlinear vibrations.For simplicity, letp
=
(
4
/
3
β
)
ρ
(
ω
o
2
-
ω
2
)
,
q
=
(
4
/
3
β
)
F
o
,
m
n, and A
=
B
-
(
p
/
3
B
) (i.e., Vieta’s substitution [31]). Equation (5) can be rewritten as
(6)
B
3
+
q
-
p
3
27
B
3
=
0
,
⇒
(7)
B
6
+
q
B
3
-
p
3
27
=
0
.
If B
3 is considered as an independent unknown, (7) is a “modified” quadratic equation. Then, the analytic formulas for the cubic solutions are given below:(8a)
A
1
=
-
1
3
1
2
(
Θ
+
Ω
)
3
-
1
3
1
2
(
Θ
-
Ω
)
3
,
(8b)
A
2
=
1
+
j
3
6
1
2
(
Θ
+
Ω
)
3
+
1
-
j
3
6
1
2
(
Θ
-
Ω
)
3
,
(8c)
A
3
=
1
-
j
3
6
1
2
(
Θ
+
Ω
)
3
+
1
+
j
3
6
1
2
(
Θ
-
Ω
)
3
,where Θ
=
(
27
q
)
2
+
4
(
3
p
)
3, Ω
=
27
q.In the next step, the nonlinear stiffness can be defined as(
3
/
4
)
β
A
2 and overall panel stiffness is ρ
ω
o
2
+
(
3
/
4
)
β
A
2. The panel impedance of the (m
,
n) mode is given by
(9)
Z
P
,
m
n
=
F
o
,
m
n
V
P
,
m
n
=
2
ρ
ξ
ω
ω
N
+
j
[
ρ
(
ω
2
-
ω
o
2
)
-
(
3
/
4
)
β
A
2
]
ω
,
where j
=
-
1
= complex number; ξ is the panel damping ratio. V
P
,
m
n is the modal panel velocity. Note that ω
N is the nonlinear peak frequency, instead of the linear natural frequency, ω
o in [32] (see Appendix B for the derivation of ω
N). When it is the case of small amplitude vibration or linear vibration, ω
N is equal to ω
o.Consider the overall panel velocity contributed from the modal velocities and find the overall panel impedance:(10)
V
P
=
∑
m
M
∑
n
N
F
o
Λ
m
n
Λ
m
n
′
Z
P
,
m
n
,
⇒
(11)
Z
P
=
F
o
V
P
=
(
∑
m
M
∑
n
N
Λ
m
n
Λ
m
n
′
Z
P
,
m
n
)
-
1
,
where Λ
m
n
′
=
(
∫
0
b
∫
0
a
sin
(
m
π
x
/
a
)
sin
(
n
π
y
/
b
)
d
x
d
y
)
/
a
b. According to [33], the sound absorption of two linearly vibrating plates with different boundary conditions was very close. It was concluded that the boundary condition would not affect the sound absorption significantly. That is why only one boundary condition case is considered here.Consider the linear case (or small amplitude case) in the model representing the panel vibration and the corresponding modal and overall panel impedances (i.e., (9), (11)). It is noted that, for the linear vibration, the fundamental harmonic balance can lead to the exact solution (no higher harmonic terms are required). Hence the modal and overall wall impedances are given below:
(12)
Z
W
,
m
n
=
2
ρ
W
ξ
W
ω
ω
W
+
j
[
ρ
(
ω
2
-
ω
W
2
)
]
ω
,
(13)
Z
W
=
(
∑
m
M
∑
n
N
Λ
m
n
Λ
m
n
′
Z
W
,
m
n
)
-
1
,
where ξ
W
,
ρ
W, and ω
W are the wall damping factor, density, and natural frequency


## 2.2. Air Pumping (Helmholtz Resonance)

In Figure1, the impedance of the air pumping along the tube mounted on the panel absorber is obtained here. The differential equation for the air mass pumping in/out along the tube is given by [29]
(14)
ρ
a
L
′
d
2
Λ
d
τ
2
+
(
R
r
+
R
w
)
S
d
Λ
d
τ
+
P
(
τ
)
=
0
,
where Λ
= air mass displacement, P
(
τ
)
= acoustic pressure excitation, R
r
=
ρ
a
c
a
k
2
S
2
/
4
π
= damping due to radiation resistance, R
w
=
2
ρ
a
L
′
S
α
w
= damping due to thermoviscous resistance, L
′
=
L
+
1.4
a
t
= effective tube length, α
w
=
(
1
/
a
t
c
a
)
(
η
ω
/
2
ρ
a
)
0.5
(
1
+
(
γ
/
Pr
)
)
= absorption coefficient for wall losses, and ρ
a is the air density; L
′ is the effective length of the tube with unflanged outer end; k is the wave number; L is the tube length; a
t is the radius of the tube; S is the cross section area of the tube; η is the air viscosity; γ is the ratio of specific heat; Pr is Prandtl number.Similar to the overall panel impedance in (9), the impedance of air pumping along the tube is given below:
(15)
Z
H
′
=
(
(
R
r
+
R
w
)
/
S
)
ω
+
j
ρ
a
L
′
ω
2
ω
.
Using (15), the air mass velocity is given by
(16)
Z
H
′
=
P
o
V
H
′
⟹
V
H
′
=
P
o
Z
H
′
,
where P
o = acoustic pressure magnitude.Consider the average velocity over the panel surface(17)
V
H
=
V
H
′
σ
H
,
where σ
H
= the ratio of tube area to panel area.Then the overall impedance of air pumping is obtained by substituting (17) into (16):
(18)
Z
H
=
Z
H
′
σ
H
.


## 2.3. Microperforation

In Figure1, the impedance of the microholes over the panel surface is obtained here. According to [9, 10], the real and imaginary parts of the acoustic impedance of a microhole are given below:(19a)
Z
M
,
R
′
=
ρ
a
c
a
(
0.147
t
d
2
)
(
9
+
100
d
2
f
32
+
1.768
f
d
2
t
)
,
(19b)
Z
M
,
I
′
=
ρ
a
c
a
1.847
f
t
(
1
+
1
9
+
50
d
2
f
+
0.85
d
t
)
,where Z
M
′
=
Z
M
,
R
′
+
j
Z
M
,
I
′
= the impedance of a microhole, f is frequency, t is panel thickness, and d is the perforation diameter. ρ
a and c
a are air density and sound speed.Then, the overall impedance of all microholes over the panel is given by(20)
Z
M
=
Z
M
′
σ
,
where σ is the perforation ratio.


## 2.4. Air Cavity

In Figure1, the impedance of the air cavity is obtained here. The acoustic velocity potential within a rectangular cavity is given by the following homogeneous wave equation [1]:
(21)
∇
2
ϕ
-
1
c
a
2
∂
2
ϕ
∂
τ
2
=
0
,
where ϕ is the velocity potential function.The air particle velocities in thex, y, and z directions and pressures within the air cavity can be given by ∂
ϕ
/
∂
x
,
∂
ϕ
/
∂
y
,
∂
ϕ
/
∂
z, and -
ρ
a
(
∂
ϕ
/
∂
τ
), respectively.The boundary conditions of the rectangular cavity to be satisfied are(22a)
∂
ϕ
∂
x
|
x
=
0
=
∂
ϕ
∂
x
|
x
=
a
=
0
;
(22b)
∂
ϕ
∂
y
|
y
=
0
=
∂
ϕ
∂
y
|
y
=
b
=
0
,
(22c)
∂
ϕ
∂
z
|
z
=
0
=
0
;
(22d)
∂
ϕ
∂
z
|
z
=
-
D
=
V
D
,where a and b are the length and width of the rectangular cavity or the panel and V
D is the average velocity at z
=
D
= cavity depth. Note that the cavity impedance of no wall vibration is derived here and used into the sound absorption formulation in the next subsection which can consider both the panel and wall vibration effects and is derived using the electroacoustic analogy.By applying the boundary conditions in (22a) and (22b), the solution of (21) can be expressed as
(23)
ϕ
=
∑
u
=
0
U
∑
w
=
0
W
[
L
u
w
cosh
⁡
(
μ
u
w
z
)
+
N
u
w
sinh
⁡
(
μ
u
w
z
)
]
×
cos
⁡
(
u
π
x
a
)
cos
⁡
(
w
π
y
b
)
e
i
ω
τ
,
where μ
u
w
=
(
(
u
π
/
a
)
2
+
(
w
π
/
b
)
2
)
-
(
ω
/
c
a
)
2, u and w are the acoustic mode numbers, U and W are the numbers of acoustic modes used in the x and y directions, and L
u
w and N
u
w are coefficients to be determined in the following step.Substituting (23) into (22c) and (22d) gives(24a)
∂
ϕ
∂
z
|
z
=
0
=
0
⟹
N
u
w
=
0
,
(24b)
∂
ϕ
∂
z
|
z
=
D
=
V
D
e
i
ω
τ
⟹
L
u
w
=
-
∫
0
a
∫
0
b
V
D
cos
⁡
(
u
π
x
/
a
)
cos
⁡
(
w
π
y
/
b
)
d
x
d
y
κ
u
w
μ
u
w
sinh
⁡
(
μ
u
w
D
)
,where κ
u
w
=
∫
0
a
∫
0
b
cos
⁡
(
u
π
x
/
a
)
2
cos
⁡
(
w
π
y
/
b
)
2
d
x
d
y.By inputting (24a) and (24b) into (23), the pressure at z
=
D is obtained and given below:
(25)
F
D
=
∑
u
=
0
U
∑
w
=
0
W
[
j
ρ
a
ω
coth
⁡
(
μ
u
w
D
)
κ
u
w
μ
u
w
a
a
a
a
a
a
a
a
a
×
coth
⁡
(
μ
u
w
D
)
κ
u
w
μ
u
w
∫
0
a
∫
0
b
V
D
cos
⁡
(
u
π
x
a
)
cos
⁡
(
w
π
y
b
)
d
x
d
y
]
×
cos
⁡
(
u
π
x
a
)
cos
⁡
(
w
π
y
b
)
.
The average pressure force at z
=
D is then given by taking integration over the panel area
(26)
F
¯
D
=
∫
0
a
∫
0
b
F
D
cos
⁡
(
u
π
x
/
a
)
cos
⁡
(
w
π
y
/
b
)
d
x
d
y
a
b
=
V
D
j
ρ
a
ω
∑
u
=
0
U
∑
w
=
0
W
[
κ
u
w
′
κ
u
w
coth
⁡
(
μ
u
w
D
)
μ
u
w
]
,
where κ
u
w
′
=
(
∫
0
a
∫
0
b
cos
⁡
(
u
π
x
/
a
)
cos
⁡
(
w
π
y
/
b
)
d
x
d
y
)
2
/
a
b.Finally, the impedance of the air cavity is given by(27)
Z
cav
=
F
¯
D
V
D
=
j
ρ
a
ω
∑
u
=
0
U
∑
w
=
0
W
[
κ
u
w
′
κ
u
w
coth
⁡
(
μ
u
w
D
)
μ
u
w
]
.
Note that since even pressure distribution is considered, then u
,
w
=
0,2
,
4
,
…. If a and b are less than 0.3 m, then the frequencies of the fundamental resonances parallel to the cavity length or width are higher than 1000 Hz (note that 1000 Hz is not within the frequency range concerned in this study). Then, in this case, only the mode numbers, u
=
0 and w
=
0, are considered. The impedance can be approximated by
(28)
Z
cav
≈
-
j
ρ
a
ω
cot
(
ω
c
a
D
)
.


## 2.5. Electroacoustic Analogy

According to [34], the acoustic impedance of a double panel absorber can be analogous to that of the electrical circuit. The acoustic impedance is given below:
(29)
Z
dou
=
Z
p
,
1
+
Z
cav
,
1
+
(
Z
cav
,
1
)
2
Z
p
,
2
+
Z
cav
,
1
+
Z
cav
,
2
,
where Z
p
,
1 and Z
p
,
2
= acoustic impedance of the 1st and 2nd panels; Z
cav
,
1 and Z
cav
,
2
= acoustic impedance of the 1st and 2nd cavities.If the impedance of the 2nd cavity is set to zero, that is, equivalent to the case of a panel absorber backed by a flexible wall, the overall impedance in (29) is rewritten as
(30)
Z
o
=
Z
com
+
Z
cav
+
(
Z
cav
)
2
Z
W
+
Z
cav
,
where Z
com
=
(
Z
M
Z
P
Z
H
)
/
(
Z
M
Z
P
+
Z
P
Z
H
+
Z
H
Z
M
)
= combined impedance. Z
M
= impedance of the microperforation; Z
P
= acoustic impedance of the panel absorber; Z
H
= impedance of the air pumping; Z
W
= impedance of the wall.If the wall is perfectly rigid (i.e., no vibration), the natural frequency of wallω
W in (12)→
∞. Hence, Z
W
,
m
n, Z
W
→
∞ and (
Z
cav
)
2
/
(
Z
W
+
Z
cav
)
≈
0. Equation (30) can be rewritten as
(31)
Z
o
=
Z
com
+
Z
cav
.
Then the absorption coefficient of the absorber α
o for normal incidence can be calculated by the well-known formula (see [29]):
(32)
α
o
=
4
Re
(
Z
o
)
(
1
+
Re
(
Z
o
)
)
2
+
(
Im
⁡
(
Z
o
)
)
2
.


## 3. Results and Discussions

Using (32), the sound absorption is obtained for the cases considered in this section. Each panel absorber is made of aluminum panel. The material properties are Young’s modulus E
=
7
×
10
10
N
/
m
2, Poisson’s ratio ν
=
0.3, and mass density ρ
=
2700
kg
/
m
3. The sound speed and air density are 340 m/s and 1.2 kg/m3, respectively. Air viscosity η
=
1.85
×
10
-
5
Pa
·
s; the ratio of specific heat γ
=
1.402; Prandtl number Pr
=
0.71. Various excitation levels, damping factors, panel sizes, and so forth are considered and their effects on the sound absorption performances are studied in the following paragraphs.Figures2 and 3 present comparisons between the frequency-absorption curves obtained from the proposed method and numerical integration method [32]. The results show that there is an absorption peak due to the microperforation around 178 Hz. The well-known “jump phenomenon” can be seen on both curves. The results obtained from the two methods are generally in reasonably good agreement, although some deviations are observed at the absorption peaks around 422 Hz in Figure 2 and 390 Hz in Figure 3. Besides, small differences between the jump frequencies (i.e., 464 and 470 Hz in Figure 2 and 410 and 420 Hz in Figure 3) are also found. The deviations are caused by that the damping term in the proposed formulation is proportional to the nonlinear peak frequency ω
N, instead of the linear natural frequency ω
o, which was adopted in [32]. The excitation level in Figure 3 is lower than that in Figure 2. Therefore, the structural vibration in Figure 3 is less nonlinear (i.e., ω
N is closer to ω
o) and the deviation between the peak values from the two methods is smaller. Note that in [32], the numerical integration method did not deliver the unstable solutions. Therefore, only stable results obtained by the proposed method in Figure 3 are compared with the numerical results in [32]. Besides, the unstable results are not obtainable in practical environments and not very useful for practical engineering purpose.Figure 2
Comparison between the results from the proposed classical and numerical methods (t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, ξ
=
0.01, σ
=
0.5
%, d
=
0.4 mm, and κ
=
5.8).Figure 3
Comparison between the results from the proposed classical and numerical methods (t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, ξ
=
0.01, σ
=
0.5
%, d
=
0.4 mm, and κ
=
2.9).Figures4(a)–4(c) present the sound absorption plotted against the excitation frequency for various panel resonant frequencies. In each of these three figures, there are two nonlinear solution types. The “jump up” or “jump down” solution is obtained by sweeping the excitation frequency from “high to low” or “low to high”. In Figures 4(a)–4(c), the linear (1,1) mode panel resonant frequencies of the three cases are 387 Hz, 172 Hz, and 97 Hz, respectively. The absorption peak frequency due to the microperforation effect is 178 Hz. It can be seen that (1) if the panel resonant frequency is higher than the absorption peak frequency due to the microperforation effect, the panel vibration can enhance and widen the absorption bandwidth and (2) if the panel resonant frequency is close to or lower than the absorption peak frequency, the panel vibration degrades the absorption performance and the peak absorption is deteriorated.(a) The effect of the (1,1) mode vibration (ω
o
= 387.25 × 2π Hz, t
=
0.8 mm, a
=
b
=
0
.
1 m, D
=
250 mm, ξ
=
0.01, σ
=
0.5
%, d
=
0.4 mm, and κ
=
10). (b) The effect of the (1,1) mode vibration (ω
o
= 172.11 × 2π Hz, t
=
0.8 mm, a
=
b
=
0.15 m, D
=
250 mm, ξ
=
0.01, σ
=
0.5
%, d
=
0.4 mm, and κ
=
10). (c) The effect of the (1,1) mode vibration (ω
o
= 96.81 × 2π Hz, t
=
0.8 mm, a
=
b
=
0.2 m, D
=
250 mm, ξ
= 0.01, σ
=
0.5
%, d
=
0.4 mm, and κ
=
10).
(a)
(b)
(c)Figures5(a) and 5(b) present the sound absorption plotted against the excitation frequency for various excitation levels. The “jump down” solutions are shown in Figure 5(a) (i.e., sweeping the excitation frequency from “high to low”) while the “jump up” solutions are in Figure 5(b) (i.e., sweeping the excitation frequency from “low to high”). The absorption peak around 178 Hz is due to the microperforation effect and is not significantly affected by the excitation level. It is noted that in the cases of κ
=
1, there is no jump phenomenon as the excitation force is quite small (i.e., linear case). Besides, it can be seen that (1) in Figure 5(a) the higher the excitation force, the wider the absorption peak due to the panel vibration and (2) in Figure 5(b) if the panel vibration is linear (or low excitation level), the absorption peak is very narrow and not very useful for widening the absorption bandwidth. Figures 6(a) and 6(b) present the sound absorption plotted against the excitation frequency for various damping ratios. The “jump down” solutions are shown in Figure 6(a) while the “jump up” solutions are in Figure 6(b). The absorption peak due to the microperforation effect is not significantly affected by the panel damping ratio. Besides, it can be seen that, (1) in Figure 6(a), the higher the damping ratio, the narrower the absorption peak due to the “jump down” panel vibration and the lower the “jump down” frequency and, (2) in Figure 6(b), the absorption peak due to the “jump up” panel vibration is not significantly affected by the damping ratio.(a) The effect of excitation level (low to high frequency excitation,ω
o
= 387.25 × 2π Hz, t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, ξ
=
0.01, σ
=
0.5
%, and d
=
0.4 mm). (b) The effect of excitation level (high to low frequency excitation, ω
o
=
387.25
×
2
π
H
z, t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, ξ
=
0.01, σ
=
0.5
%, and d
=
0.4 mm).
(a)
(b)(a) The effect of damping ratio (low to high frequency excitation,ω
o
= 387.25 × 2π Hz, t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, σ
=
0.5
%, d
=
0.4 mm, and κ
=
10). (b) The effect of damping ratio (high to low frequency excitation, ω
o
= 387.25 × 2π Hz, t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, σ
=
0.5
%, d
=
0.4 mm, and κ
=
10).
(a)
(b)Figures7(a) and 7(b) present the sound absorption and vibration amplitude plotted against the excitation frequency. Note that this case does not consider any perforation effect and other effects. There are two peaks in each of the two figures, which are due to the (1,1) and (1,3) mode resonances, respectively. It can be seen that the peaks due to the (1,1) mode resonance are more nonlinear. As the two peaks are far from each other, no strong mode coupling effect is induced. In Figure 7(b) the vibration amplitude is almost linearly increasing from 100 Hz to 286 Hz while the sound absorption is almost linearly increasing from 100 Hz to 150 Hz only and slowly and nonlinearly increasing from 150 Hz to 286 Hz. Besides, the absorption peak due to the (1,3) mode resonance is much more significant than the vibration peak. It can be implied that higher mode responses are important for absorption but not for vibration.(a) The absorption peaks due to the (1,1) and (1,3) mode vibrations (low to high frequency excitation,t
=
0.5 mm, a
=
b
=
0.15 m, D
=
250 mm, and k
=
5). (b) The vibration peaks due to the (1,1) and (1,3) mode vibrations (low to high frequency excitation, t
=
0.5 mm, a
=
b
=
0.15 m, D
=
250 mm, and κ
=
5).
(a)
(b)Figures8(a) and 8(b) present the sound absorption plotted against the excitation frequency and show the effects of air pumping (Helmholtz resonance) and microperforation. In Figure 8(a), the peak frequencies of air pumping and microperforation are around 100 Hz. It can be seen that the absorption bandwidth of the case with both effects is much wider and its peak absorption is much higher than the cases with air pumping or microperforation only. The two effects can interact with each other and significantly enhance the absorption performance. In Figure 8(b), the peak frequencies of air pumping and microperforation are quite far from each other. The enhancement of the absorption performance due to the two effects is not as good as that in Figure 8(a).(a) The effects of the air pumping and microperforation (t
=
0.3 mm, a
=
b
=
0.1 m, D
=
150 mm, σ
=
0.5
%, d
=
0.3 mm, L
=
10 mm, and a
t
=
5 mm). (b) The effects of the air pumping and microperforation (t
=
0.3 mm, a
=
b
=
0.1 m, D
=
100 mm, σ
=
0.28
%, d
=
0.3 mm, L
=
10 mm, and a
t
=
5 mm).
(a)
(b)Figures9(a) and 9(b) present the sound absorption plotted against the excitation frequency for various damping ratios and show the effect of linear wall vibration. The peak frequencies of wall panel and microperforation are around 80 Hz and 178 Hz, respectively. It can be seen that the wall vibration does not affect the absorption performance significantly and just induces an abrupt change around 80 Hz. The magnitude of the abrupt change depends on the damping ratio (i.e., the higher the damping ratio, the smaller the abrupt change). Figures 10(a) and 10(b) present the sound absorption plotted against the excitation frequency and show the effects of microperforation and linear and nonlinear vibrations. It can be seen that the effects of microperforation and nonlinear panel vibration are positive and significant while the effect of linear wall vibration is negative but not significant.(a) The effects of linear wall vibration and microperforation (ω
W
=
80
×
2
π
Hz, ρ
w
=
240
/
m
2, t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, ξ
W
=
0.02, σ
=
0.5
%, and d
=
0.4 mm). (b) The effects of linear wall vibration and microperforation (ω
W
=
80
×
2
π
Hz, ρ
w
=
240
/
m
2, t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, ξ
W
=
0.01, σ
=
0.5
%, and d
=
0.4 mm).
(a)
(b)(a) The effects of microperforation and linear and nonlinear vibrations (low to high frequency excitation,ω
o
=
387.25
×
2
π
Hz, ω
W
=
80
×
2
π
Hz, ρ
w
=
240
kg
/
m
2, t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, ξ
=
ξ
W
=
0.01, σ
=
0.5
%, d
=
0.4 mm, and κ
=
10). (b) The effects of microperforation and linear and nonlinear vibrations (high to low frequency excitation, ω
o
=
387.25
×
2
π
Hz, ω
W
=
80
×
2
π
Hz, ρ
w
=
240
kg
/
m
2, t
=
0.8 mm, a
=
b
=
0.1 m, D
=
250 mm, ξ
=
ξ
W
=
0.01, σ
=
0.5
%, d
=
0.4 mm, and κ
=
10).
(a)
(b)


## 4. Conclusions

In this study, the analytic absorption formulation has been developed for the panel absorber under the effects of microperforation, air pumping, and linear and nonlinear vibration. From the predictions, it can be concluded that (1) if the panel resonant frequency is higher than the absorption peak frequency due to the microperforation effect, the panel vibration can enhance and widen the absorption bandwidth; (2) if the panel resonant frequency is close to or lower than the absorption peak frequency, the panel vibration degrades the absorption performance or the peak absorption is deteriorated; (3) the higher the excitation force, the wider the absorption peak due to the panel vibration; (4) if the panel vibration is linear (or low excitation level), the absorption peak is very narrow and not very useful for widening the absorption bandwidth; (5) the absorption bandwidth of the case with the air pumping and microperforation effects is much wider and its peak absorption is much higher than the cases with any one of these two effects. If the peak frequencies of air pumping and microperforation are far from each other, the enhancement of the absorption performance is small; and (6) the wall vibration does not affect the absorption performance significantly and just induces a small abrupt change on the absorption bandwidth around the wall resonant frequency.



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*Source: 906506-2014-07-23.xml*