Deformation Dependent Sound Absorption Property of a Novel Magnetorheological Membrane Sound Absorber

A novel membrane sound absorber based on the magnetorheological membrane (MRM) is developed for active sound absorption. Due to its good flexibility and stretch-ability, the MRM consisting of carbonyl iron particles (CIPs) and polydimethylsiloxane elastomer matrix can be easily deformed. The deformation of MRM is investigated by the digital image correlation method. The off-plane displacement is positively related to both of the CIPs mass fractions and magnetic field strength. The sound absorption performance of MRM sound absorber is investigated and it is found that the thickness of the membrane, CIPs mass fractions, and air cavity length behind the membrane significantly influence the sound absorption performance. The magnetic field can adjust the sound absorption frequency without affecting the high acoustical absorption coefficients. The double-layer membrane structure has two sound absorption peaks within the testing frequency range and further improves the frequency adjustability of the sound absorber. Therefore, it is expected to be a particularly promising alternative for active sound absorption. Finally, the numerical solutions calculated by the equivalent circuit method also support the experimental results.

Introduction

The membrane sound absorber is a widely used sound absorption structure, which is of thin thickness, high sound absorption coefficients and wide tunable frequency range (Zhao et al., 2017; Gai et al., 2018; Liu et al., 2019a), and has attracted great interest to researchers who want to reduce sound emissions in the last decades. A typical membrane absorber is composed of a single membrane and an air cavity behind it. The sound absorption properties of membrane absorbers are mainly influenced by the surface density, membrane tension and air cavity length (Jimenez et al., 2016; Ahmed et al., 2019). In recent years, most of the researches were focused on the traditional membrane sound absorbers. Maa firstly proposed the basic theory and design principles of the micro-perforated panel absorbers (Maa, 1975). His theoretical work laid the foundation for other similar sound absorption structures (Reto and Kurt, 2015; Takeshi and Kimihiro, 2015; Arenas and Ugarte, 2016). Kang and Fuchs concluded the equivalent circuit method for different kinds of membrane sound absorbers (Kang and Fuchs, 1999). Kimihiro et al. investigated the resonance effect of micro-perforated membrane absorbers and discussed the absorption mechanisms of membrane-type absorbers (Kimihiro et al., 2009). Very recently, Zhu et al. installed a lightweight membrane-type resonator in the back cavity of perforated membrane absorbers to combine into a compound sound absorber and further improved the adjusting ability for sound absorption (Zhu et al., 2018b).

The membrane sound absorber with tunable acoustic properties is very important for their practical application. However, the acoustic properties of the existing membranes are usually un-tunable once the materials are prepared. Magnetorheological (MR) materials are a kind of smart materials (Ju et al., 2016; Xu et al., 2018) whose mechanical properties can be controlled by applying an external magnetic field. The mechanical properties and magnetic controlled deformation of MR materials have been systematically investigated. Due to the tunable mechanical characteristics, MR materials have been widely used in vibration control (Fu et al., 2016; Liu et al., 2019b; Zhang et al., 2019), magnetic sensing (Ding et al., 2018; Ren et al., 2018; Hu et al., 2020), magnetic controlled movement (Lum et al., 2016; Chen et al., 2018; Ubaidillah et al., 2019) and robot manufacturing (Eric et al., 2014; Feng et al., 2017; Vien et al., 2019). In consideration of their easy deformation, tunable mechanical properties and contactless magnetic actuation, the MR materials are expected to have wonderful performance in sound absorption. However, few works have been reported on employing MR materials in sound absorption and investigating their acoustic mechanism.

In this work, the MR membrane (MRM) is used to replace the normal membrane in traditional membrane absorbers to develop a novel magnetorheological sound absorber. The magnetic field dependent mechanical properties, deformation and sound absorption capacity were investigated. A finite element simulation was carried out to confirm the experimental results of the deformation. The sound absorption performance of the MRM sound absorber was measured and the MRM sound absorber had excellent sound absorption properties and frequency adjustable performance. The equivalent circuit method was employed to calculate the sound absorption coefficient and the numerical results agreed with the experimental discussion. Therefore, the magnetorheological membrane sound absorbers are expected to be a particularly promising alternative for active sound absorption.

Experiment

Materials

Carbonyl iron particles (CIPs) were brought from BASF in Germany and the average size of CIPs is 7μm. ${\text{Fe}}_3{\text{O}}_4$ particles were produced by Chengxin Metal Materials Co., Ltd. The polydimethylsiloxane (PDMS) precursor and curing agent (Sylgard 184) were obtained from Dow Corning.

Preparation of the Magnetorheological Membranes

The fabrication processes of the magnetorheological membranes were schematically illustrated in Figure 1. The PDMS matrix, curing agent and iron particles were mixed up in different proportions and the mixture was vacuumed to remove trapped bubbles for 30 min. The ratio of the matrix to the curing agent was 10:1 and the CIPs mass fractions were set as 10, 20, 30, and 50 wt% respectively. After that, the mixture was poured on the rotor of a spin coater. The rotor rotated at 1,000–1,500 rpm for 1 min and the mixture was homogenized to be a membrane. Then, the membrane was cured at 100°C for 10 min to be vulcanized. Finally, the prepared magnetorheological membranes were fixed by the rigid ring with a radius of 15 mm and thickness of 2 mm for sound absorption test.

FIGURE 1

FIGURE 1. Schematic diagram of the material preparation process.

Magnetic Induced Deformation of Magnetorheological Membranes

The digital image correlation (DIC) method was employed to investigate the magnetic induced deformation of MRMs and the scheme of the commercial DIC analyzer (PMLAB DIC-3D, Nanjing PMLAB Sensor Tech. Co., Ltd.) was shown in Figure 4A. DIC is a far-field and full field measurement with strong anti-interference ability and high measurement accuracy (Gao et al., 2015; Enrico et al., 2017). It has been widely applied in measuring the deformation of materials or structures (Zhang et al., 2005; Jiang et al., 2007). The MRM was fixed by a rigid ring and sprayed with white paint spots evenly as marks. Two pictures of the painted membrane were taken from different directions and the location information of the marked points were recorded. Then, the membrane deformed under the magnetic field and another two pictures were taken to record the deformation. Finally, the deformation of the MRM was calculated. In this experiment, the deformation of MRMs with different components was measured to investigate the influence factors of displacement. The prepared MRMs were placed 2 mm above the central axis of an electromagnet coil. The outer and inner diameters of the electromagnet coil were 95 and 50 mm respectively. The size of the electromagnet coil was large enough to ensure that the magnetic field around the sample was relatively uniform. The magnetic fields at the center of the MRM surface were adjusted from 60 and 180 mT by controlling the current in the electromagnet coil.

Sound Absorption of the Magnetorheological Membrane Sound Absorber

The sound absorption tests were carried out by an acoustic test system. The system consists a signal generator, a power amplifier, a sound transmission tube, a sound reflection tube, two acoustic sensors and a computer used for calculation (Figure 2). The MRM was fixed by a rigid ring with a radius of 15 mm and thickness of 2 mm and placed on the front end of the sound reflection tube. The sound waves used in experimental tests were pink noise, which was one of the most commonly used acoustic waves in acoustic tests.

FIGURE 2

FIGURE 2. Schematic diagram of the acoustic tube.

When the samples were tested, the acoustical signal was generated from the signal generator controlled by the computer, amplified by the power amplifier, and spread into the sound transmission tube. Then, the acoustical signal was reflected at the sample and returned to the sound transmission tube. In the whole process, two acoustic sensors located at the sound transmission tube recorded the amplitude and phase information of the acoustic signal. In order to guarantee the accuracy of test results, the power amplifier was supposed to make sure that the incident acoustic signals were controlled between 90 and 110 dB. Finally, the acoustic signals were processed with the transfer function method in the computer to calculate the sound absorption curve. When the magnetic field was applied, the backboard was replaced by an electromagnet coil (Figure 2), which could play the same role as the backboard.

Result and Discussion

Characterization of Magnetorheological Membranes

The physical pictures and SEM images of the MRMs were shown in Figures 3A–D. The surface of MRMs was smooth and the colors of the surface darkened gradually as the increasing of CIPs mass fractions (Figure 3A). Subtle ripples on the membrane surface observed in the SEM were due to the rotation during the preparation process (Figure 3B). CIPs were evenly distributed in the PDMS matrix (Figure 3C). MRMs were 40–180 μm in thickness and they tended to be stuck together because of their extra thin thickness, thus they were usually fixed on the framework during the experiment. When the rheological properties were investigated, MR elastomers with different mass fractions were prepared as disks with 0.5 mm in thickness and 10 mm in radius. Magnetic field scanning tests were carried out by the commercial rheometer (Physica MCR 301, Anton Paar) and Figure 3F shows their rheological properties. The initial storage moduli of MR elastomers were only 0.29 MPa, which meant that they were relatively easy to deform. The storage modulus increased with increasing of the magnetic field and tended to be stable when the magnetic field exceeded 400 mT. At the same time, the samples with higher mass fraction were strengthened more obviously by the magnetic field. Therefore, the mechanical properties of MR materials can be controlled by the external magnetic field. The hysteresis loops were also measured to characterize the magnetization of MRMs (Figure 3E). The magnetization had an important influence on the mechanical behavior in a magnetic field. With increasing of CIPs from 10 to 50 wt%, the saturation magnetizations were proportional to CIPs mass fractions and could reach to 96.26 emu/g. These high magnetizations must be responded for large magnetic deformation.

FIGURE 3

FIGURE 3. Diagram of the samples with different mass fractions (A), SEM images of the surface (B) and the longitudinal section (C), thickness of the sample under the optical microscope (D), storage modulus (E) and hysteresis loops (F) of the samples with different mass fractions.

Magnetic induced deformation of Magnetorheological Membranes

When MRMs were exposed to a magnetic field, the ferromagnetic particles in MRMs were magnetized under the magnetic field and magnetic dipoles were induced within adjacent ferromagnetic particles. The magnetic dipoles were subject to magnetic forces in the magnetic field and drove the matrix to deform. The magnetic dipole moment $\stackrel{\rightharpoonup }{m}$ and the force on the magnetic dipoles $\stackrel{\rightharpoonup }{F}$ were controlled by the following expressions (Boyer and Timothy, 1998):

$\stackrel{\rightharpoonup }{B}=\left(3\widehat{n}\widehat{n}·\stackrel{\rightharpoonup }{m}-\stackrel{\rightharpoonup }{m}\right){\mu }_0/4\pi r^3(1)$

$\stackrel{\rightharpoonup }{F}=\nabla (\stackrel{\rightharpoonup }{m}·\stackrel{\rightharpoonup }{B})(2)$

where $\stackrel{\rightharpoonup }{B}$ is the magnetic flux density, $\stackrel{\rightharpoonup }{m}$ is the magnetic dipole moment, ${\mu }_0$ is the permeability of vacuum, r is the radius of the magnetic particles and $\widehat{n}$ is the unit vector of r. The hysteresis loops displayed in Figure 3E demonstrated the magnetization of the MR materials under a certain magnetic field. Obviously, the samples with higher CIPs mass fractions performed stronger magnetization.

The deformations of MRMs were measured by the DIC method. The MRM was fixed flat on a frame and set on the central axis of an electromagnet coil. At the initial state, its off-plane displacement was zero. Then the MRM sagged inward slowly with increasing of the magnetic field. Figure 4B showed the image of the membrane deformation and the membrane was significantly deformed by applying the magnetic field. The results of the deformation test were displayed in Figure 4E, where the solid data points represented the experimental off-plane displacement of the membrane. The max off-plane displacement obtained by applying a 180 mT magnetic field to the 50 wt% CIP-MRM could reach as large as 1.69 mm. The deformation was significantly related to the magnetic field strength. A larger deformation was obtained under a larger magnetic field, because the stronger magnetic dipoles were induced in the CIPs were magnetized into stronger magnetic dipoles under large magnetic fields. At the same time, the mass fraction of CIPs also had a distinct influence on the deformation. The schematic diagram of the deformation of membranes with different mass fractions were showed in Figure 4D. The mass fractions of CIPs directly determined the number of magnetic dipoles. The MRMs with higher mass fractions can be magnetized to form more magnetic dipoles which further led to stronger magnetic force.

FIGURE 4

FIGURE 4. Schematic diagram of the DIC (A). Deformation of the MRMs under a magnetic field (B). Simulation result (C) and deformation diagram (D) of MRMs. Comparison of experimental and theoretical results for the max off-plane displacements (E).

The finite element simulation of the deformation was carried out to calculate the numerical value of the deformation under different magnetic field. The simulation was carried out by the COMSOL Multiphysics. The solids included the MRM, electromagnet coil, iron core, and air region. The current in the electromagnet coil was adjusted to turn the magnetic field to be similar to the magnetic field intensity in the forenamed experiment. Each solid was endowed with the corresponding material properties including the mechanical and magnetic parameters. The inside selection was chosen as the mesh operation and then the deformation could be obtained. The deformed shape of the membrane was displayed in Figure 4C. The dotted curves represented the numerical off-plane displacement of the membrane (Figure 4E). The max numerical off-plane displacement was 1.78 mm, which was closely similar to the experimental result. The numerical and experimental curves had the same tend and the experimental results were consistent with the numerical consequences.

Sound Absorption of the Magnetorheological Membrane Sound Absorber

When a sound wave encountered a wall or other obstacle, part of the sound energy was reflected, and part of the sound energy was absorbed by the wall or obstacle and converted into heat energy. The other part of the sound energy was transmitted to the other side. The sound absorption capacity of a certain material or structure was called the sound absorption coefficient. The definition of the sound absorption coefficient can be expressed as follows (Soltani and Zerrebini, 2012):

$\alpha =\frac{E_a+E_t}{E}=\frac{E-E_r}{E}=1-r(3)$

where $\alpha$ is the sound absorption coefficient, r is the sound reflection coefficient, E is the total sound energy incident on the material, $E_a$ is the sound energy absorbed by the material, $E_t$ is the sound energy transmitted through the material, $E_r$ is the sound energy reflected by the material. The sound absorption coefficient is normally between 0 and 1. The materials with lager sound absorption coefficient have better sound absorption performance. Generally, the materials with a sound absorption coefficient smaller than 0.2 have little sound absorption capacity and they are not suitable for sound absorption. The materials with a sound absorption coefficient greater than 0.4 can be used for sound absorption in practical application. Furthermore, if the sound absorption coefficient is larger than 0.5, this kind of material is considered to have excellent sound absorption capacity.

The sound absorption tests were carried out by the acoustic tube under different conditions. The thickness of MRMs, mass fractions of CIPs, air cavity length behind the membrane, and magnetic field strength were main factors that affected the sound absorption performance. The thickness and CIPs mass fraction of the control group were 40 μm and 50 wt% respectively. As shown in Figures 5A-D, the sound adsorption curves were unimodal in the measured frequency range. The MRM and air cavity behind the membrane formed a sound-absorbing structure together and this structure had its own natural frequency. When the sound wave was incident on the sound absorption structure, the acoustic energy would be transformed into the thermal energy and kinetic energy due to the damping and vibration. If the frequency of the incident sound wave was close to the natural frequency of the sound absorption structure, the resonance phenomenon occurred. The vibration of the sound absorption structure and the sound energy dissipation increased significantly, thus the sound absorption coefficient reached the maximum value. Although the natural frequency of a composite structure is difficult to estimate in a simple way, it is usually positively related to modulus and inversely related to mass or surface density. Obviously, most MRM sound absorbers have excellent sound absorption properties at their natural frequencies where the sound absorption coefficient is close to 1. This is because the MRM is thin and easy to deform, and it can vibrate intensely at the resonant frequency.

FIGURE 5

FIGURE 5. The influences of the air cavity length behind the membrane (A), the thickness of the membrane (B), mass fractions of CIPs (C), the magnetic field (D) on the sound absorption curves. The peak frequency and the sound absorption wideband corresponding to the above image (E–H). The sound absorption curves of the double-layer membrane structure with the varied length of the air cavity (I–K). Influences of the magnetic field on the double-layer membrane structure (L).

Here, the sound absorption wideband is defined as the frequency range where the sound absorption coefficient is larger than half of the max sound absorption coefficient. The sound absorption wideband is usually positively related to the max sound absorption coefficient and the peak frequency (Lee and Lee, 2007; Zhu et al., 2018b). The peak value of the sound adsorption and sound absorption wideband were displayed in Figures 5E-H. The air cavity length behind the membrane has the most significant influence on the sound absorption frequency. The peak sound absorption frequency changed from 4,260 to 2,088 Hz when the air cavity length behind the membrane increased from 2 to 8 mm (Figures 5A,E). The peak sound absorption coefficients were all close to 1 in Figure 5A. Therefore, the air cavity length behind the membrane can adjust the natural frequency in a wide frequency range without changing the good deformability of MRMs. Specially, the sound absorption frequency can be adjusted drastically while ensuring a high sound absorption coefficient.

On the contrary, with increasing of MRMs thickness, the peak sound absorption shifted to the lower frequency and the sound absorption coefficient decreased (Figure 5B). Though the natural frequency was adjusted by increasing the membrane thickness, the MRMs became harder and more difficult to be vibrated. In this case, less sound energy was consumed by vibration, thus the sound absorption coefficient decreased. Moreover, the membrane with lower CIPs mass fraction exhibited lower sound absorption coefficient, because it was too soft for effective vibration (Figure 5C). The magnetic field can attract MRMs to deform in the direction of the magnetic field and its influence on the sound absorption properties was similar to the air cavity length behind the membrane (Figure 5D). They both adjusted the sound absorption properties by changing the air cavity length. Here, the magnetic field can tune the whole structure without touching or modifying structure, and this characteristic is of great significance in practical application.

Furthermore, a double-layer membrane structure was investigated to improve the control of the sound absorption frequency. The double-layer membrane structure was developed by putting another membrane in the air cavity of the initial structure and formed two air cavities (Figure 2 sectional view). The sound absorption tests of the double-layer membrane structure were investigated. Different from the single-layer membrane, there were two sound absorption peaks on the sound absorption curve of the double-layer membrane structure (Figures 5I–L), thus it has two closer natural frequencies. The air cavities length behind two membranes was the most effective parameter to control the sound absorption properties. It can adjust the sound absorption frequency easily and maintain a high sound absorption coefficient simultaneously. The distance between two membranes was recorded as $D_1$ and the distance between the back membrane and the container wall was recorded as $D_2$ (Figure 6C). The two sound absorption frequencies were significantly related to $D_1$ and $D_2$ as shown in Figures 5I-K. The increased $D_1$ or $D_2$ would decrease the sound absorption frequency. However, the effects of them were not exactly the same. When $D_1$ remained constant and $D_2$ increased, the low frequency peak moved to low frequency and the high frequency peak stayed still. Correspondingly, when $D_2$ remained constant and $D_1$ increased, the high frequency peak moved to low frequency and the low frequency peak was kept. If $D_1$ and $D_2$were changed at the same time (their sum kept constant), the two sound absorption peaks would move closer or away to each other. By combining these two adjustment methods, it is convenient to design a sound absorber with tuning sound absorption frequency within the tested frequency range. The influence of the magnetic field on the double-layer membrane structure was also investigated. Similar to the single-layer membrane structure, the magnetic field can decrease the air cavities length and lead the sound absorption peak shift to the high frequency. Here, due to the limitation of the small magnetic field, the adjustment range is not particularly wide.

FIGURE 6

FIGURE 6. Schematic diagram (A) and equivalent circuit (B) of the single-layer membrane structure, schematic diagram (C) and equivalent circuit (D) of the double-layer membrane structure.

Numerical Solutions of Sound Absorption Coefficients

In order to further understand the sound absorption performance of the sound absorption structure, an equivalent circuit method was employed to predict the sound absorption curves (Kang and Fuchs, 1999). The equivalent circuit was displayed in Figure 6, in which R and L were the acoustic resistance and reactance of the membrane, D was the air cavity length and $Z_c$ was the impedance of the air cavity. The impedance of the entire equivalent circuit $Z_0$ can be calculated by this equivalent circuit. The normalized specific acoustic impedance of the entire equivalent circuit z was defined as follows:

$z=\frac{Z_0}{\rho c}(4)$

Then, the sound absorption coefficient can be calculated by a classic formula:

$\alpha =\frac{4Re\left(z\right)}{{[1+Re\left(z\right)]}^2+{\left[Im\left(z\right)\right]}^2}(5)$

where z is the normalized specific acoustic impedance of the entire equivalent circuit and it consists of two parts, the acoustic impedance of the membrane $z_m$6 and the acoustic impedance air cavity $z_c$7:

$z_m=\frac{R+jL}{\rho c}=r+j\omega m(6)$

$z_c=-jcot\frac{\omega D}{c}(7)$

where $\rho$ is the density of air, c is the sound velocity in air, m is the surface density of the membrane, $\omega$ is the angular frequency and $\omega =2\pi f$, f is the frequency, D is the air cavity length, r is the normalized specific sound resistance and $r=80.42d{f}^{1/2}$, d is the membrane thickness. According to the equivalent circuit diagram in Figure 6B, the normalized specific acoustic impedance z can be calculated as follows:

$z=z_m+z_c=r+j(\omega m-cot\frac{\omega D}{c})(8)$

Then, the final expression of the sound absorption coefficient can be expressed as:

$\alpha =\frac{4r}{{[1+r]}^2+{[\omega m-cot\frac{\omega D}{c}]}^2}(9)$

The sound absorption coefficient reaches the maximum value when $\omega m=\cot \left(\frac{\omega D}{c}\right)$ and the maximum absorption coefficient is:

${\alpha }_{max}=\frac{4r}{{[1+r]}^2}(10)$

For the case of double membranes, there are two air cavities between the membranes and the container wall. The expression of equivalent impedance can be derived with the equivalent circuit diagram in Figure 6D as follows:

$z= r_1+j\omega m_1+{\left[\frac{1}{z_{D1}}+\frac{1}{r_2+j\omega m_2+z_{D2}}\right]}^{-1}= r_1+j[\omega m_1-\cot \left(\frac{\omega D_1}{c}\right)]+\frac{co{t}^2(\omega D_1/c)}{r_2+j[\omega m_2-cot\left(\omega D_1/c\right)-cot(\omega D_2/c)]}(11)$

Then the sound absorption coefficient of double membranes can be calculated by bringing the Eq. 11 into the Eq. 5, as shown in Figure 7. The solid curves and the dash dot curves represented the experiment results and the numerical results respectively. Figures 7A,B showed the influences of the air cavity length and magnetic field strength on the sound absorption curves. The curves of numerical solutions basically coincided with the experimental results. The simulation of the double-layer membrane structure was displayed in Figures 7C,D. The sound absorption frequencies of the numerical curves and the experimental curves were slightly different, but the sound absorption curves of them were similar overall.

FIGURE 7

FIGURE 7. Comparison of experimental and numerical results: the air cavities length (A), the magnetic field (B), the length of the front cavity of double-layer membrane structure (C), the length of the back cavity of double-layer membrane structure (D).

The parameters studied in this work all indirectly adjusted the sound absorption coefficient by changing the acoustic impedance of the structure. The membrane thickness and CIPs mass fractions changed the acoustic impedance of the membrane. The air cavity length behind the membrane and the magnetic field strength determined the acoustic impedance of the air cavity. More importantly, the increased thickness and mass fractions of CIPs also affected the deformability of the membrane. Therefore, with increasing of the MRM thickness and CIPs mass fractions, the max sound absorption coefficient decreased. Contrastively, the air cavity length behind the membrane and the strength of magnetic fields only changed the acoustic impedance of the air cavity to adjust the sound absorption coefficient but not the properties of MRMs, so they had little negative influence on the max sound absorption coefficient. As a result, the tunable range of the frequency for this kind of sound absorption structure is wide and the adjustment can be achieved by the remote magnetic field without touching the structure.

Finally, the MR membranes with ${\text{Fe}}_3{\text{O}}_4$ particles (${\text{Fe}}_3{\text{O}}_4$-MRMs) were also investigated as a comparison (Figure 8). The saturation magnetization of ${\text{Fe}}_3{\text{O}}_4$ particles was smaller than CIPs. The mass fraction and thickness of the ${\text{Fe}}_3{\text{O}}_4$-MRMs were kept as the same to CIP-MRMs. Then, the deformation behavior of the ${\text{Fe}}_3{\text{O}}_4$-MRMs was tested and the results showed the max off-plane displacement of ${\text{Fe}}_3{\text{O}}_4$-MRMs was 1.27 mm. In comparison to the CIP-MRMs, the simulated deformation result for ${\text{Fe}}_3{\text{O}}_4$-MRMs was significantly lower under the same conditions, which must be responded for the weak magnetically induced dipoles (Figure 8A). Figures 8B,C displayed the comparison of the sound absorption curves and sound absorption frequency of the two kinds of MR membranes. Obviously, the frequency adjustment ability of ${\text{Fe}}_3{\text{O}}_4$-MRMs was relatively poorer, which should be due to the smaller deformation. Therefore, the deformation is the key to control sound absorption performance. The larger deformation gives chances to adjusted the sound absorption frequency in a wider frequency range.

FIGURE 8

FIGURE 8. Deformation and sound absorption properties of the ${\text{Fe}}_3{\text{O}}_4$-MRMs: deformation simulation diagram (A), comparison of the sound absorption curves between ${\text{Fe}}_3{\text{O}}_4$-MRMs and CIP-MRMs (B), comparison of the peak frequency between the ${\text{Fe}}_3{\text{O}}_4$-MRMs and CIP-MRMs (C).

Conclusion

This work reported a novel sound absorber based on MRMs and the sound absorber exhibited a magnetic field tunable absorption frequency with a wide range absorption efficiency. The thin MRMs were easy to be deformed under an external magnetic field. The max off-plane displacement reaches as large as 1.69 mm when a 180 mT magnetic field is applied on the 50 wt% CIP-MRM. The numerical analysis carried out by the finite element method confirmed that the off-plane displacement was positively related to the CIPs mass fractions and the magnetic field strength. Then, the influence of the membrane thickness, CIPs mass fractions, air cavity length behind the membrane, and the strength of the magnetic field on the sound absorption properties were investigated. The air cavity length and the strength of the magnetic field not only adjusted the sound absorption frequency but also maintained the high sound absorption coefficient. As a result, the strength of the magnetic field can tune the sound absorption structure without touching or modifying the structure, thus it is of high potential for active sound absorption and remote control.

Data Availability Statement

The original contributions presented in the study are included in the article, further inquiries can be directed to the corresponding author/s.

Author Contributions

CS performed all the experiments and wrote the draft of the manuscript. XC, XZ, SX and XG revised and discussed the manuscript.

Funding

The financial supports from the National Natural Science Foundation of China (Grant No. 11822209, 12072338, 11702174), Joint Fund of USTC-National Synchrotron Radiation Laboratory (KY2090000055) and the Strategic Priority Research Program of the Chinese Academy of Sciences (Grant No. XDB22040502) are gratefully acknowledged.

Conflict of Interest

The authors declare that the research was conducted in the absence of any commercial or financial relationships that could be construed as a potential conflict of interest.

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