Front. Phys. Frontiers in Physics Front. Phys. 2296-424X Frontiers Media S.A. 1333198 10.3389/fphy.2023.1333198 Physics Original Research FEM/Wideband FMBEM coupling based on subdivision isogeometry for structural-acoustic design sensitivity analysis Chen et al. 10.3389/fphy.2023.1333198 Chen Xiuyun 1 Huang Yajun 2 Zhou Zhongbin 1 Xu Yanming 1 * 1 Henan International Joint Laboratory of Structural Mechanics and Computational Simulation, School of Architecture and Civil Engineering, Huanghuai University, Zhumadian, China 2 College of Intelligent Construction, Wuchang University of Technology, Wuhan, China

Edited by: Yilin Qu, Northwestern Polytechnical University, China

Reviewed by: Mengxi Zhang, Tianjin University, China

Xudong Li, Chinese Academy of Sciences (CAS), China

 *Correspondence: Yanming Xu, xuyanming@ustc.edu 06 12 2023 2023 11 1333198 04 11 2023 24 11 2023 Copyright © 2023 Chen, Huang, Zhou and Xu. 2023 Chen, Huang, Zhou and Xu

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A computer simulation approach known as the isogeometric (IGA) method may directly use the surface information of geometric model. In 3D computer graphics, Loop subdivision surfaces are a common method for creating complicated shapes. In this study, we propose a coupling algorithm that utilizes Loop subdivision surfaces and a direct differentiation method for the computation of acoustic-fluid-structure interaction and the performance of structural-acoustic sensitivity analysis. This algorithm combines the finite element method (FEM) and wideband fast multipole boundary element method (FMBEM). Because of that the proposed method is of a great ability of integrating the numerical calculation and computer-aided modeling, the current technique can deliver results quickly and accurately. The numerical prediction of the effects of vibrating structures with arbitrary shape within sound field is made feasible by the FEM/Wideband FMBEM technique. Calculation examples are provided to show the applicability and effectiveness of the suggested method.

 loop subdivision surfaces IgA fluid-structure interaction design sensitivity analysis direct differentiation method section-at-acceptance Interdisciplinary Physics 1 Introduction

The elastic structures in heavy fluid resulting in acoustic radiation or scattering is a common issue in underwater acoustics. It is possible to give the analytical solutions of the issues with acoustic fluid-structure interaction phenomenon while the structure is with simple boundary conditions and geometry [1,2]. However, as it comes for real-world issues which usually have complex geometries, providing an analytical solution becomes harder and even impossible, thus effective simulation techniques are needed.

FEM is extensively utilized to study the dynamic behavior of issues involving fluid-structure interactions, acoustics, and structures. The FEM has several drawbacks for modeling infinite domains, though. Because it offers good accuracy and simple mesh generation, BEM has been widely employed to calculate acoustic issues. The Sommerfeld radiation condition [3] is met, especially for external acoustic issues. The Galerkin technique has been frequently used in BEM implementation to solve the boundary integral problem numerically [4]. However, the collocation approach, has historically been popular in the engineering field. Hence, the coupled FEM/BEM technique [5,6] is suitable for studying fluid-structure interaction problems. However, the high computational expense remains a challenge when performing coupling analysis of underwater structural-acoustic problems using the FEM/Conventional BEM (CBEM) algorithm. This is primarily because CBEM generates a dense and non-symmetric coefficient matrix. Many techniques have been used to speed up the integral problem solution, including fast multipole method (FMM), the adaptive cross approximation methodology and fast direct solver. Martinsson and Rokhlin [7,8] introduced the fast direct solver, which works well for issues requiring moderately ill-conditioned matrices and immediately builds a compressed factorization of the matrix inverse. The adaptive cross approximation methodology [9], developed by Bebendorf and Rjasanow, has the capability to generate blockwise low-rank approximations from the BEM matrices. This methodology is particularly suitable for problems that require a large number of iterations. FMM [10–12] has been developed to reduce memory requirements while speeding up the solving of the CBEM system of equations. In reality, the Helmholtz equation has two versions of the Fast Multipole Method (FMM), namely, the original FMM and the diagonal form. However, it is well-known that both of these versions tend to fail outside of their optimal frequency ranges in some manner. On the other hand, the aforementioned issues can potentially be resolved by utilizing wideband FMM [13–18]. This advanced technique combines the original FMM with the diagonal form FMM, leading to more efficient solutions. Therefore, the challenges related to large-scale fluid-structure interaction problems can be effectively resolved through the utilization of the coupling approach based on FEM/fast multipole boundary element method (FEM/FMBEM) [19–23]. Furthermore, this study proposes the utilization of the FEM/Wideband FMBEM coupling method to tackle the intricate problems associated with fluid-structure interactions.

Through the use of appropriate software, FEM and BEM may be implemented—a process known as computer-aided engineering (CAE). Nowadays, industry 4.0 and digital twin technologies are being developed with the use of CAE simulation. The models created by CAD software must, however, be transformed into simulation-ready models as part of the preprocessing stage used by modern CAE. The CAE’s most time-consuming manual intervention phase, the geometric model data transfer stage produces geometry inaccuracies. The integration of geometric modeling and numerical simulation using isogeometric analysis [24–26] with boundary element method (IGABEM) [27,28] is suggested as a solution to this issue. By using IGABEM, geometric mistakes and time-consuming preprocessing steps may be avoided and numerical simulation can be carried out straight from the precise models. Since its inception, IGABEM has been used to address a variety of issues, including those related to elastic mechanics [27–30], potential issues [15], wave-resistance [31], fracture mechanics [32,33], electromagnetics [34–39], and structural optimization [40–46].

In addition to the benefits already discussed, IGABEM offers significant benefits for modelling acoustics issues. Numerous engineering fields have found extensive use for acoustics, including noise control, underwater navigation using sonar, ultrasound imaging for medical purposes, seismology, electroacoustic communications, etc. Numerous numerical simulation techniques have significant challenges when it comes to acoustics for that the sound wave may travel through semi-infinite domains. By shifting the acoustic field from a semi-infinite domain to the boundary of the domain, IGABEM can get around this problem. Simpson [16,47] applied IGABEM to acoustics. Acoustic optimization [37,48,49] with IGABEM was studied.

In the framework of the IGABEM, several sorts of geometric modeling approaches have been extensively researched. The ability to build multi-resolution geometries with complex forms and topologies makes the subdivision surface approach among them very promising [51–56]. There are two types of subdivision surfaces: Catmull-Clark and Loop method. Structure-acoustic interaction [1,57,58] and acoustic optimization [59–63] were both addressed using IGABEM based on Loop subdivision surfaces. The goal of the current effort is to merge Loop subdivision surfaces with IGABEM for sensitivity analysis. Additionally, we’ll speed up the solution process using wideband FMM.

Designers are increasingly considering passive noise management by altering the geometry of the construction. Particularly for thin shell structures, this structural-acoustic optimization has considerable promise for minimizing radiated noise [64]. Acoustic design sensitivity analysis is a crucial component in the process of acoustic design and optimization, as it allows for understanding the effect of geometry changes on the acoustic performance. In a comprehensive review by Marburg [65], advancements in structural-acoustic optimization for passive noise reduction were discussed. The global finite difference method (FDM) has been extensively employed for structural-acoustic optimization due to its ease of implementation [66–69]. However, this approach doesn’t work so well, particularly while considering several design elements simultaneously. To get over this issue, employ the adjoint variable approaches [70,71] or the direct differentiation method [72]. The sensitivity analysis for interaction issues is widely recognized as the most time-consuming step in gradient-based optimization. In our study, we aim to accelerate the calculation process by employing a direct differentiation approach for structural-acoustic sensitivity analysis in the FEM/Wideband FMBEM method.

In this study, we propose the incorporation of wideband FMBEM in the coupling of structural-acoustic sensitivity analysis and present the formulation for sensitivity analysis in the coupled FEM/BEM analysis. We advocate for the adoption of coupled FEM/Wideband FMBEM to address fluid-structure interaction problems and conduct structural-acoustic sensitivity analysis. To eliminate the geometry inaccurices, Loop subdivision scheme is applied to the sensitivity analysis of an underwater fluid-structure coupling problem. Through the computation of various numerical examples, we have demonstrated the accuracy and effectiveness of the proposed strategy.

 2 Structural-acoustic coupling deduction 2.1 Subdivision scheme

In computer animation and graphics, it is of great advantages of using Subdivision surfaces [73,74] since their emergence in the 1970s. They may also be accessed in most industrial CAD solid modeling applications. Subdivision surfaces are frequently mentioned as a technique for continually fine-tuning and smoothing a control mesh so a smooth limit surface could be produced. They may also be regarded as the extension of splines to arbitrarily linked meshes for FEM and BEM.

A rough polygon mesh is transformed into a smooth surface using subdivision techniques. The creation of a smooth surface using subdivision method—which is usually classified as interpolating schemes—involves a constrained, repeating refinement process that starts with an initial control mesh. Due to the refinement characteristic inherited from splines, all control meshes generated during subdivision refinement accurately represent the same spline surface.

The structural-acoustic coupling analysis in this study is carried out utilizing the Loop subdivision scheme [59]. The quadrisection refinement of a triangular mesh in a construction of loop subdivision is shown in Figure 1. A vertex’s valence is the edges number that link it. When N = 6, a vertex is considered regular, and when N ≠ 6, it is considered irregular. Each triangle is split into four smaller triangles by adding a new vertex at the middle of each edge. As indicated in Eqs 1, 2, the positions of new vertices and edge points may be determined from the previous level. x i v k + 1 = 5 8 x i v k + 3 8 N ∑ i = 1 N x i k , x i e k + 1 = 3 8 x 1 k + 1 8 x 2 k + 3 8 x 3 k + 1 8 x 4 k , where

iv is the i-th vertex point
i.e., is the i-th edge point

Templates for vertex and edge points with regular and irregular shapes.

In reality, there are too many nodes, making it impossible to achieve smooth surfaces with few subdivisions. Another method for creating limit surfaces for any degree of refinement is to create an elementwise map using linear combinations of Box-splines basis functions on triangular control meshes. For further details, please refer to Chen et al.[59].

 2.2 BEM analysis

∇ 2 p x + k 2 p x = 0 , p x = p ̄ x x ∈ Γ p , q x = ∂ p x ∂ n x = i ρ ω v ̄ x x ∈ Γ q , p x = z v x x ∈ Γ z , where

p is sound pressure
k is wave number
n is external normal direction of the boundary
q is normal derivative of p
i is imaginary unit, i = − 1
ρ is structural density
ω is frequency of the incoming force
v is normal velocity
z is acoustic impedance
Γ p is Dirichlet boundary condition
Γ q is Neumann boundary condition
Γ z is Robin boundary condition
( ) ̄ is known function given on the border

Equation 3 describes a acoustic wave which is time-harmonic in the Helmholtz equation, and Eq. 4 serves as an expression for the boundary conditions. A boundary integral equation (BIE) specified on the Γ can be created from Eqs 3–5. c x p x + ∫ Γ F x , y p y d Γ y = ∫ Γ G x , y q y d Γ y , where

x is source point
y is field point
c(x) is 1/2 if the boundary Γ is smooth in the vicinity of the source point x
p(x) is intensity of the incoming wave at source point x
p(y) is sound pressure at field point y
G(x, y) is Green’s function
q(y) is normal derivative of p(y)
F(x, y) is normal derivative of G(x, y)

Equations 6, 7 gives the expression of Green’s function for acoustic problems in two and three dimensional problems, respectively. G x , y = i 4 H 0 1 k r , G x , y = e i k r 4 π r , r = y − x . When the boundary Γ is smooth around the source point x, the derivative of the integral representation in Eq. 5 with respect to the outer normal can be expressed as Eq. 8. 1 2 q x + ∫ Γ ∂ F x , y ∂ n x p y d Γ y = ∫ Γ ∂ G x , y ∂ n x q y d Γ y .

It is common knowledge that applying a single Helmholtz boundary integral equation to issues involving external boundary values may be challenging due to nonuniqueness. In order to effectively solve the nonuniqueness problem, the Burton-Miller approach [75]—which is a linear combination of Eqs 5, 8—is used in this study. The computation of the singular boundary integrals introduced by Eqs 5, 8 can also be performed directly and efficiently using the Cauchy principal value and the Hadamard finite part integral method [72].

If the boundary Γ is divided into elements, the system can be obtained [76] and can be expressed as Eq. 9 by assembling the equations for collocation points located in the center of each element. H p = G q + p i , where

H is the coefficient matrix of the vector p
G is the coefficient matrix of the vector q
p i is the nodal pressure caused by the incoming wave
2.3 FEM analysis

The complete structural-acoustic simulation approach was described by Fritze et al. [6], and related expressions are supplied here. The structure response is determined by analyzing of frequency-response under the assumption that a harmonic load performs on the structure. Equation 10 derives the linear system of structural-acoustic equation. K + i ω C − ω 2 M u = f where

K is stiffness matrix
i is imaginary unit, i = − 1
ω is excitation frequency of the harmonic load
C is damping matrix
M is mass matrix
u is nodal displacement vector
f is complete excitation

It is crucial to take into account that, because of damping, the steady-state response may have the same frequency as the applied load but a different phase angle. To handle non-harmonic imposed loads, the time-dependent forces can be examined in the frequency domain, enabling the use of Eq. 10. To address the effect of acoustic pressure on structural surfaces, a coupling matrix is introduced. This matrix facilitates the transfer of the structural nodal load from the fluid effect to the fluid nodal pressure. Then, Eq. 11 could be used to express the complete excitation, combining the acoustic load and the structural load. f = C s f p + f s , C sf = ∫ Γ int N s T n N f d Γ , where

C sf is coupling matrix
p is fluid nodal pressure
C sf p is acoustic load
f s is structural load
N s is interpolation function for structural domain
N f is interpolation function for fluid domain
n is external normal direction of the structural surface
Γ is interaction surface between the structural and fluid domains

The structural nodal load from the fluid effect is directed to fluid nodal pressure via the coupling matrix C sf . The nodal displacement could then be obtained from Eq. 10, as shown in Eq. 12. u = K + i ω C − ω 2 M − 1 f .

2.4 FEM-BEM coupling analysis

The exact formulas of FEM/BEM modeling were published by Fritze et al. [6], and related expressions are supplied in this part. The continuity constraint over the interaction surface—as shown in Eq. 13—connects the governing equations as illustrated in the above section. Then, the normal velocity v may be written as a function with the displacement u, according to Eq. 14. q = − i ω ρ v , v = i ω S − 1 C fs u , S = ∫ Γ int N f T N f d Γ , C fs = C s f T . We can get Eq. 15 by inserting Eqs 13, 14 into Eq. 9. H p = ω 2 ρ G S − 1 C f s u + p i . Equations 10, 11, 15 can be connected to form a equation system, as shown in Eq. 16. K + i ω C − ω 2 M − C sf − ω 2 ρ G S − 1 C f s H u p = f s p i .

The direct iterations on Eq. 16 converge rather slowly, and directly solving the system equation would demand far more computational power and storage space. We present the following method as an alternative to utilizing an iterative solver to resolve the above non-symmetric linear equation. The coupled boundary element equation (6) shown in Eq. 17 may be obtained by putting Eq. 12 into Eq. 15. H p − G W C s f p = G W f s + p i , W = ω 2 ρ S − 1 C f s A − 1 , A = K + i ω C − ω 2 M . By using a sparse direct solver, the equation linear system in Eq. 17 could be solved. To speed up the solution, FMM and the Generalized Minimum Residual (GMRES) iterative solver are used.

In this study, Loop subdivision is introduced in the model discretization in order to realize the FEM-BEM coupling and the ensuing sensitivity analysis.

 3 Sensitivity analysis for shape design

Finding the optimum design parameters specifying the intended form of the given structure under specified restrictions is the aim of shape optimization. Calculating the gradients of stated cost functions is done using shape design sensitivity analysis. The direction in which to look for the best values of the design variables may then be decided using the acquired gradients. As a result, the first and most crucial phase in the design and optimization of acoustic shapes is often acoustic form sensitivity analysis [72,77]. The direct method utilizes the chain rule of differentiation to compute the sensitivity of the performance function. This process begins with determining the sensitivity of the variables before proceeding to compute the performance function sensitivity. Because it is so directly tied to the analytical process, this strategy is quite popular.

By differentiating Eqs 5, 8 with respect to any arbitrary design variable, assuming that the boundary Γ is smooth around the source point x, we can derive Eqs 18, 19. 1 2 p ̇ x = ∫ Γ G ̇ x , y q y − F ̇ x , y p y d Γ y + ∫ Γ G x , y q ̇ y − F x , y p ̇ y d Γ y + ∫ Γ G x , y q y − F x , y p y d Γ ̇ y . 1 2 q ̇ x = ∫ Γ ∂ G x , y ∂ n x ̇ q y − ∂ F x , y ∂ n x ̇ p y d Γ y + ∫ Γ ∂ G x , y ∂ n x q ̇ y − ∂ F x , y ∂ n x p ̇ y d Γ y + ∫ Γ ∂ G x , y ∂ n x q y − ∂ F x , y ∂ n x p y d Γ ̇ y . For two dimensional problems, we have Eq. 20. G ̇ x , y = − i k 4 H 1 1 k r r ̇ , F ̇ x , y = − i k 4 H 1 1 k r y ̇ j − x ̇ j n j y r + r , j n ̇ j y + i k 2 4 H 2 1 k r r ̇ r , j n j y , r ̇ = r , j y ̇ j − x ̇ j . For three dimensional problems, we have Eq. 21. G ̇ x , y = − e i k r 4 π r 2 1 − i k r ∂ r ∂ y i y ̇ i − x ̇ i , F ̇ x , y = e i k r 4 π r 3 3 − 3 i k r − k 2 r 2 ∂ r ∂ n y ∂ r ∂ y j − 1 − i k r n j y y ̇ j − x ̇ j − e i k r 4 π r 2 1 − i k r ∂ r ∂ y i n ̇ i y , r ̇ = r , j y ̇ j − x ̇ j . The singular boundary integrals introduced by Eqs 18, 19 can be computed directly and efficiently using the Cauchy principal value and the Hadamard finite part integral method [72].

By differentiating Eq. 17 with respect to the design variable, the sensitivity analysis for shape design using the coupling FEM-BEM can yield Eq. 22. H p ̇ − G W C s f p ̇ = G ̇ X + G Y − H ̇ p , X = W C s f p + f s , Y = W ̇ C s f p + f s + W C sf ̇ p + f s ̇ , W ̇ = ω 2 ρ S − 1 ̇ C fs A − 1 + S − 1 C fs ̇ A − 1 + S − 1 C fs A − 1 ̇ .

Since the matrices are full and asymmetric, it takes a lot of computing time to directly solve Eq. 22 using conventional BEM. However, it is possible to speed up the computational process using FMM and GMRES. The matrix-vector products in Eqs 17, 22 are accelerated using wideband FMM, and the FEM-BEM coupling formula and the associated sensitivity equation are solved using the iterative solver GMRES.

 4 Numerical examples

Several numerical tests are conducted to examine the validity and dependability of the established methodology in this section. In each case, the FEM uses shell elements whereas the discontinuous linear boundary elements are applied for acoustic analysis. All calculations are performed using a customized internal Fortran 95/2003 algorithm.

4.1 Sphere with an incoming sound wave

This section examines the sound field of an thin spherical shell that is centered at location (0, 0, 0), while accounting for an incoming sound wave with an amplitude of 1.0 in positive x direction, as shown in Figure 2. The following are the materials and geometrical elements used in this example.

Radius 4.0 m
thickness 0.04 m
elasticity modulus 2.10 × 1011 Pa
Poisson’s ratio 0.3
structural density 7.86 × 103 kg/m3
fluid density 1.00 × 103 kg/m3
sound velocity in water 1.482 × 103 m/s

The sphere model and its mesh plot. (A) The sphere model. (B) Mesh of the sphere model.

Figure 3 gives the results at position (10, 0, 0). Figure 3A displays the analytical and numerical solutions. The GMRES implementation with the wideband FMM technique is employed to accelerate the solution of linear systems without preconditioning. The discretized thin-shell model consists of 25,392 elements. The wideband FMM approach keeps the high accuracy of BEM, as the numerical and analytical answers present the good agreement which can seen in the figure.

Sound pressure and sensitivity at (10,0,0) for spherical shell model. (A) Sound pressure at (10,0,0). (B) Sensitivity to radius at (10,0,0). (C) Sensitivity to thickness at (10,0,0).

Figures 3B, C shows, respectively, how sensitive the structure’s surface is to sound pressure in relation to the radius and thickness of the sphere. Basically, these graphs demonstrate a good agreement between the analytical and numerical results. Figure 3 shows that the sound pressure sensitivity grows significantly at resonance peaks, and the lower frequency range is crucial for this spherical shell model because the sound pressure there is substantially higher and more responsive to thickness and radius.

The results are shown in Figures 4, 5, respectively, for the positions (20, 0, 0) and (40, 0, 0). The curves for the same physical quantity at various locations, as shown in Figures 3, 4, 5—Figures 3A, 4A, 5A for sound pressure, Figures 3B, 4B, 5B for sensitivity to radius, and Figures 3C, 4C, 5C for sensitivity to thickness—all show a similar pattern of fluctuation.

Sound pressure and sensitivity at (20,0,0) for spherical shell model. (A) Sound pressure at (20,0,0). (B) Sensitivity to radius at (20,0,0). (C) Sensitivity to thickness at (20,0,0).

Sound pressure and sensitivity at (40,0,0) for spherical shell model. (A) Sound pressure at (40,0,0). (B) Sensitivity to radius at (40,0,0). (C) Sensitivity to thickness at (40,0,0).

 4.2 Submarine model under an incoming sound wave

This section focuses on the underwater submarine model’s scattering sound field when influenced by an incoming plane wave [78]. The plane wave propagates predominantly along the x-axis and has an incidence wave amplitude of 1.0 Pa. The thickness of the submarine model is 0.01 m, and the sub has a length of 9.2 m. The origin of the coordinate is in the middle of the axial length of the submarine, and the x-axis is along the axial length of the submarine. The submarine model constructed using Loop subdivision scheme is shown in Figure 6, which has a total of 19,016 elements.

The submarine model.

Several calculation points are selected. Figure 7A gives the sound pressure changing with frequency at point (50, 0, 0) and Figure 7B illustrates the changing of its sensitivity to thickness. These two data demonstrate that the lower frequency range, given the existing material and geometrical parameters, is a vital region for this submarine model, as the sound pressure is noticeably greater and more sensitive to thickness there.

Sound pressure and sensitivity at point (50,0,0) for submarine model. (A) Sound pressure at (50,0,0). (B) Sensitivity to thickness at (50,0,0).

The computation of sound pressure at location (100, 0, 0) and (150, 0, 0) is shown in Figures 8A, 9A, respectively. Figures 8B, 9B depicts the sensitivity of sound pressure at point (100, 0, 0) and (150, 0, 0) to shell thickness, respectively. Figures 7A, 8A, 9A show comparable patterns in the sound pressure curves at the places (50, 0, 0), (100, 0, 0), and (150, 0, 0). As seen in Figures 7B, 8B, 9B, the sensitivity of sound pressure at (50, 0, 0), (100, 0, 0), and (150, 0, 0) also demonstrates a similar pattern. Additionally, and in line with predictions, the sound pressure and its sensitivity to thickness both decline with increasing distance from the structure.

Sound pressure and sensitivity at point (100,0,0) for submarine model. (A) Sound pressure at (100,0,0). (B) Sensitivity to thickness at (100,0,0).

Sound pressure and sensitivity at point (150,0,0) for submarine model. (A) Sound pressure at (150,0,0). (B) Sensitivity of sound pressure to thickness at (150,0,0).

 5 Conclusion

The simulation of acoustic-structure interaction and sensitivity analysis are conducted using a coupling approach that combines the Finite Element Method (FEM) and Boundary Element Method (BEM). FEM is applied to model structural elements of the issue. To eliminate the need for meshing the acoustic domain, the boundary of the structure being analyzed is discretized using the BEM. FMM is applied to expedite the matrix-vector output. IGABEM enables direct structural-acoustic interaction and sensitivity analysis from CAD models without the requirement for meshing, thereby eliminating any geometric errors. For coupled structural-acoustic systems, equations are derived for the sound pressure sensitivity. To prove the accuracy and practicality of the recommended strategy, calculation examples are given. The recommended method may be used to quantitatively predict how design parameters would affect the sound field in real-world scenarios.

Reduced order isogeometric boundary element methods for CAD-integrated shape optimization of electromagnetic scattering.

 Data availability statement

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

 Author contributions

XC: Data curation, Formal Analysis, Writing–original draft. YH: Methodology, Resources, Software, Writing–original draft. ZZ: Investigation, Validation, Visualization, Writing–original draft. YX: Conceptualization, Project administration, Supervision, Writing–original draft.

 Funding

The author(s) declare financial support was received for the research, authorship, and/or publication of this article. The authors appreciate the financial support from Henan Provincial Key R&D and Promotion Project under Grant No. 232102220033.

 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.

 Publisher’s note

All claims expressed in this article are solely those of the authors and do not necessarily represent those of their affiliated organizations, or those of the publisher, the editors and the reviewers. Any product that may be evaluated in this article, or claim that may be made by its manufacturer, is not guaranteed or endorsed by the publisher.

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