Electroelastic Coupled-Wave Scattering and Dynamic Stress Concentration of Piezoceramics Containing Regular N-Sided Holes

Abstract

In this paper, the calculation method of dynamic stress concentration around piezoelectric ceramics containing regular n-sided holes under the action of electroelastic coupling wave was studied, and it was applied to promising barium calcium zirconate titanate material. First, electroelastic governing equations were decomposed by using the auxiliary function method, and the solution forms of the elastic wave field and electric field were obtained by using the wave function expansion method. Then, the triangular boundary was simplified to a circular boundary using the mapping function, and the corresponding modal coefficients were determined according to simplified boundary conditions. Finally, the dynamic stress-concentration factor was calculated to characterize the dynamic stress concentration. We performed numerical simulations with a correlation coefficient of (1 − x)[(Ba_0.94Ca_0.06) (Ti_0.92Sn_0.08)]-xSm₂O₃-0.06 mol% GeO₂ (abbreviated as (1 − x)BCTS-xSm-0.06G). The numerical calculation results show that the incident wave number, piezoelectric properties, shape parameters of the hole, and deflection angle have a great influence on the dynamic stress around the defect, and some significant laws are summarized through analysis.

1. Introduction

The commercialization of piezoelectric ceramics has developed rapidly in the past 10 years [1,2,3]. Opportunities for its application in the fields of piezoelectric energy harvesting, piezoelectric fuel injection, piezoelectric motors, piezoelectric printing presses, piezoelectric controlled wire guides, micropositioning systems, and so on are also increasing [4,5,6,7]. For a long time, lead zirconate titanate (Pb(Zr_1−xTi_x)O₃ or PZT) has been the main material of piezoelectric ceramics due to its excellent piezoelectric properties [8,9]. However, the production and application of PZT result in a large amount of lead pollution in the form of lead oxide and lead zirconate titanate [10,11]. In order to protect the environment, increasing attention is being paid to research of lead-free piezoelectric materials [12,13,14,15].

In the processing and application of lead-free piezoelectric materials, geometric discontinuities (holes, cuts, notches) may occur. Under complex loads and harsh conditions, stress concentration is likely to occur, resulting in fatigue cracks in the periphery, and even structural failure [16,17,18]. Furthermore, stress concentration around the geometric discontinuity is the basis of subsequent fracture and fatigue analysis, which has important practical significance.

Some scholars have applied different engineering methods to analyze the stress concentration. Smith and Kullgren et al. [19] obtained the stress intensity factor around the partial elliptical crack caused by the fastener hole on the finite-thick plate by the finite element-alternating method. In addition, Kim et al. [20] applied finite element analysis to calculate a polynomial expression for the calculation of the stress intensity factor for a lug with a through-thickness crack. Liang et al. [21] performed a series of numerical simulations on circular piezoelectric plates with holes using a special boundary element method. However, neither FEM nor BEM can obtain the analytical formula of stress factor. These numerical methods cannot reveal a clear relationship between stress concentrations and related factors (material parameters, hole shape parameters, etc.) [22,23].

Therefore, more and more researchers are trying to derive analytical solutions using elastic mechanics and complex functions. Wang et al. [24] used the Stroh-type formula to study the anti-plane problem of equilateral triangle hole cracking in transversely isotropic piezoelectric materials. Fan et al. [25] studied the inverse plane problem of edge cracks generated by equilateral triangular holes in one-dimensional hexagonal piezoelectric quasicrystals by introducing numerical conformal mapping using the Stroh-type formula. These studies only discuss a single common shape and do not discuss the effect of different shape parameters on stress concentration [26,27]. Wang et al. [28] solved arbitrary holes with edge cracks in transversely isotropic piezoelectric materials using the complex variable method and the numerical conformal mapping method. The loads used in these studies are all static. However, real-world loading conditions are often dynamic and complex.

In this paper, diffraction and dynamic stress concentration near several common-shaped holes of lead-free piezoelectric ceramics under the action of electroelastic coupled-load waves are investigated. First, we reduce the problem to a 2D inverse plane problem by setting the load to be an inverse plane shear wave. Then, the basic form of elastic wave field and electric potential solution is obtained by the wave function expansion method. Affine transformations are used to map common-shaped holes into circular holes to simplify boundary conditions. Then, according to the simplified free boundary conditions, the undetermined coefficients of the diffraction field are determined, and the analytical solution of the dynamic stress concentration factor (DSCF) around the hole is given. Finally, taking (Ba_0.85Ca_0.15)(Zr_0.1Ti_0.9)O₃ as an example, the DSCF results of common-shaped holes under different parameters are calculated and analyzed, as well as the effects of incident wave number, shape parameters and piezoelectric parameters on stress concentration.

2. Problem and Basic Equations

In order to meet the needs of engineering design, it is inevitable to open holes of various shapes on the lead-free piezoelectric ceramics. In addition, some structures may also have holes or cracks during service, and these holes may produce stress concentration or even break under the action of daily dynamic load. We intend to use incident elastic waves to simulate dynamic loads in everyday life. Among them, the dynamic stress concentration caused by the anti-plane shear wave (SH wave) is normally used as the basis for the calculation of the stress field intensity factor of the type iii dynamic fracture. Therefore, the inverse plane shear wave (SH wave) was selected as the incident wave in this paper. According to the characteristics of SH waves, the three-dimensional electroelastic coupling problem can be transformed into a two-dimensional anti-plane problem.

The hole model of arbitrary shape on the lead-free piezoelectric ceramic is shown in Figure 1. We took the centroid of the shape as the origin and the incident direction of the SH wave as the polar axis to establish a cylindrical coordinate system. Lead-free piezoelectric ceramics are set to be isotropic and uniform.

For the two-dimensional anti-plane problem, the out-of-plane displacement and in-plane electric field are only functions of coordinates $r$ and $\theta$, and all physical quantities depend only on the anti-plane displacement $w$ and in-plane electric potential $\phi$.

$$\begin{array}{l}{u}_x=u_y=0\hfill \\ w=w\left(r,\theta \right)\hfill \\ \phi =\phi \left(r,\theta \right)\hfill \end{array}$$

(1)

where $u_x$ and $u_y$ are used to describe the in-plane displacement.

In the cylindrical coordinate system, the coupling characteristics of mechanical deformation and electric field of lead-free piezoelectric ceramics can be described by the following constitutive equation:

$$\begin{array}{l}{\tau }_{rz}=c_{44}\frac{\partial w}{\partial r}+e_{15}\frac{\partial \phi }{\partial r}\\ {\tau }_{\theta z}=c_{44}\frac{1}{r}\frac{\partial w}{\partial \theta }+e_{15}\frac{1}{r}\frac{\partial \phi }{\partial \theta }\\ D_r=e_{15}\frac{\partial w}{\partial r}-{\epsilon }_{11}\frac{\partial \phi }{\partial r}\\ D_{\theta }=e_{15}\frac{1}{r}\frac{\partial w}{\partial \theta }-{\epsilon }_{11}\frac{1}{r}\frac{\partial \phi }{\partial \theta }\end{array}$$

(2)

where $c_{44}$ is the elastic constant; $e_{15}$ is the piezoelectric constant; ${\epsilon }_{11}$ is the dielectric constant. In the quasi-static electromagnetic approximation, the stress $({\tau }_{rz},{\tau }_{\theta z})$ and electric displacement $(D_r,D_{\theta })$ should satisfy the following equilibrium equation:

$$\begin{array}{l}\frac{\partial {\tau }_{rz}}{\partial r}+\frac{1}{r}\frac{{\tau }_{\theta z}}{\theta }+\frac{{\tau }_{rz}}{r}=\rho \frac{{\partial }^{2}w}{\partial t^2}\\ r\frac{\partial D_r}{\partial r}+\frac{1}{r}\frac{D_{\theta }}{\theta }+D_r=0\end{array}$$

(3)

Substituting Equation (2) into (3) and sorting it, the general equation describing the problem in the cylindrical coordinate system can be obtained as follows:

$$\begin{array}{l}{\mathrm{c}}_{44}(\frac{1}{r^2}\frac{{\partial }^{2}w}{\partial {\theta }^2}+\frac{{\partial }^{2}w}{\partial r^2}+\frac{1}{r}\frac{\partial w}{\partial r})+e_{15}(\frac{1}{r^2}\frac{{\partial }^2\varphi }{\partial {\theta }^2}+\frac{{\partial }^2\varphi }{\partial r^2}+\frac{1}{r}\frac{\partial \varphi }{\partial r})=\rho \frac{{\partial }^{2}w}{\partial t^2}\\ e_{15}(r\frac{{\partial }^{2}w}{\partial r^2}+\frac{1}{r}\frac{{\partial }^{2}w}{\partial {\theta }^2}+\frac{\partial w}{\partial r})-{\epsilon }_{11}(r\frac{{\partial }^2\varphi }{\partial r^2}+\frac{1}{r}\frac{{\partial }^2\varphi }{\partial {\theta }^2}+\frac{\partial \varphi }{\partial r})=0\end{array}$$

(4)

3. Forms of Solutions for Incident, Scattered and Electroelastic Waves

Since the differential equation to be solved is electroelastic coupling, we used the auxiliary function method for decoupling. Construct the auxiliary function $\gamma =\varphi -\frac{e_{15}}{{\epsilon }_{11}}w$ and substitute it into Equation (4):

$$\begin{array}{c}\frac{1}{r^2}\frac{{\partial }^{2}w}{\partial {\theta }^2}+\frac{{\partial }^{2}w}{\partial r^2}+\frac{1}{r}\frac{\partial w}{\partial r}=\frac{1}{c_s{}^2}\frac{{\partial }^{2}w}{\partial t^2}\\ \frac{1}{r^2}\frac{{\partial }^2\gamma }{\partial {\theta }^2}+\frac{{\partial }^2\gamma }{\partial r^2}+\frac{1}{r}\frac{\partial \gamma }{\partial r}=0\end{array}$$

(5)

where $c_s=\sqrt{\chi /{\rho }_0}$ is the propagation velocity of SH waves, $\chi =c_{44}+e_{15}{}^2/{\epsilon }_{11}$. The decoupled equations are all classical differential equations, and their solution forms can be obtained. Therefore, we can obtain the displacement field and electric potential field of the scattered wave as follows:

$$\begin{array}{l}{w}^s={\displaystyle \sum _{n=-\infty }^{\infty }{A}_n{H}_n^{(1)}(kr)}{\mathrm{e}}^{\mathrm{i}n\theta }\\ \gamma ={\displaystyle \sum _{n=0}^{\infty }{B}_n{k}^{-n}{r}^{-n}{\mathrm{e}}^{\mathrm{i}n\theta }}\\ {\varphi }^s=\frac{e_{15}}{{\epsilon }_{11}}{w}^s+\gamma \end{array}$$

(6)

where $A_n$ and $B_n$ are the undetermined coefficient used to describe the scattered elastic wave field and scattered potential field, respectively. $H_n^{\left(1\right)}(\cdot )$ is the n-th order Bessel function of the third kind. $k=\omega /c_s$ is the incident wave number. The superscript $s$ refers to the scattered wave field.

Since the SH wave is also a classical incident wave, the form of the solution of its displacement field and electric potential field can be described by the following formulas:

$$\begin{array}{c}{w}^i=w_0{\displaystyle \sum _{n=-\infty }^{\infty }{\mathrm{i}}^n{J}_n(kr){\mathrm{e}}^{\mathrm{i}n\theta }}\\ {\varphi }^i=\frac{e_{15}}{{\epsilon }_{11}}{w}^i\end{array}$$

(7)

The superscript $i$ refers to the incident wave field. The total field and total potential field of elastic waves in lead-free piezoelectric ceramics can be obtained by superimposing the incident field and scattered field:

$$\begin{array}{c}{w}^t=w^i+w^s\\ {\varphi }^t=\frac{e_{15}}{{\epsilon }_{11}}(w^i+w^s)+\gamma \end{array}$$

(8)

where the superscript $t$ refers to the total wave field. In the hole, the elastic wave field does not exist, and the electric displacement field is not equal to zero. The form of the electric displacement field in the hole can be expressed as

$${\varphi }^c={\displaystyle \sum _{n=0}^{\infty }{C}_n(k}r{)}^n{e}^{in\theta }$$

(9)

where $C_n$ is the undetermined coefficient; similar to $A_n$ and $B_n$, it needs to be determined by boundary conditions. The superscript $c$ refers to the wave field inside the hole.

4. Mapping Function

In order to simplify the boundary of regular polygons, we can introduce complex variables according to the theory of complex functions:

$$\begin{array}{l}\zeta =x+\mathrm{i}y=r(\cos \theta +\mathrm{i}\sin \theta )\\ \overline{\zeta }=x-\mathrm{i}y=r(\cos \theta -\mathrm{i}\sin \theta )\end{array}$$

(10)

Then, we need to map the polygon boundary to a unit circle using the conformal transformation. A schematic diagram of conformal mapping is shown in Figure 2.

To map the outer region of the regular n-sided hole on the $\zeta$ plane to the outer region of the unit circle in the $\eta$ plane, the mapping function for the SC transformation is given below [29]:

$$\zeta =\Omega (\eta )=R{\displaystyle {\int }_1^{\eta }{\displaystyle \prod _{j=1}^m{(t-a_j)}^{{\alpha }_j-1}dt}}+C_1$$

(11)

where the constants $R$ and $C_1$ are the shape coefficient and position coefficient of the regular n-sided hole, respectively. $R$ and $C_1$ can be calculated by selecting two sets of corresponding points. One of the sets of points is selected as the corresponding set of points at infinity on the two planes, resulting in $C_1=0$. Another set of points can be selected as a vertex of a regular polygon and a corresponding point on the circle for subsequent calculation of $R$. $m$ is the number of sides of a regular n-gon, $a_j$ is the vertex corresponding to the regular n-gon, ${\alpha }_j(j=1,2,\dots ,k)$ is the group angle of the j-th interior angle divided by $\pi$. Then,

$${\displaystyle \sum _{j=1}^m{\alpha }_j}=m+2$$

(12)

Substitute $a_j$ and ${\alpha }_j$ in Equation (11), and integrate them in the range of $1$ and $\eta$ to obtain the mapping function as follows:

$$\zeta =\Omega (\eta )=R(\eta +{\displaystyle \sum _{i=1}^s\frac{c_i}{{\eta }^{im-1}}})$$

(13)

where

$$c_1=\frac{2}{m(m-1)},c_2=\frac{m-2}{m^2(2m-1)},\cdots ,c_i={\displaystyle \sum _{i=3}^s\frac{{\displaystyle \prod _{j=2}^i(j-1)}m-2}{(i!/2)m^i(im-1)}}$$

5. Boundary Conditions and Determination of Mode Coefficients

The boundary conditions on the $\eta$ plane can be simplified as

$$\begin{array}{l}{\tau }_{\rho z}{|}_{\rho =a}=0\\ D_{\rho }{|}_{\rho =a}=D_{\rho }{}^c{|}_{\rho =a}=-{\epsilon }_{11}\frac{\partial {\varphi }^c}{\partial r}{|}_{\rho =a}\\ {\varphi }^{(t)}{|}_{\rho =a}={\varphi }^c\end{array}$$

(14)

Substitute Equation (12) into Equations (8) and (9):

$$\begin{array}{cc}\hfill w^{(t)}=& {\displaystyle \sum _{n=-\infty }^{\infty }[w_0{\mathrm{i}}^n{J}_n(k\left|\Omega (\eta )\right|)+A_n{H}_n{}^{(1)}(k\left|\Omega (\eta )\right|)]}{\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^n\hfill \\ \hfill {\varphi }^{(t)}=& \frac{e_{15}}{{\epsilon }_{11}}{\displaystyle \sum _{n=-\infty }^{\infty }[w_0{\mathrm{i}}^n{J}_n(k\left|\Omega (\eta )\right|)+A_n{H}_n{}^{(1)}(k\left|\Omega (\eta )\right|)]}{\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^n\hfill \\ & +{\displaystyle \sum _{n=0}^{\infty }{B}_n{k}^{-n}}{(\overline{\Omega (\eta ))}}^{-n}\hfill \\ {\varphi }^{(c)}=& {\displaystyle \sum _{n=0}^{\infty }{C}_n}{\left[k\left|\Omega (\eta )\right|\right]}^n{\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^n\hfill \end{array}$$

(15)

Substituting Equation (15) into (14), the boundary conditions under the conformal transformation can be obtained:

$$\begin{array}{l}{\tau }_{\rho z}{|}_{\rho =a}=0\\ \frac{k}{2}{c}_{44}(1+\frac{e_{15}{}^2}{c_{44}{\epsilon }_{11}}){\displaystyle \sum _{n=-\infty }^{\infty }{w}_0{\mathrm{i}}^n\{w_0{\mathrm{i}}^n[\frac{\eta }{\rho }\frac{{\Omega }^{\prime }(\eta )}{\left|{\Omega }^{\prime }(\eta )\right|}{J}_{n-1}(k\left|\Omega (\eta )\right|){\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^{n-1}}\\ -\frac{\overline{\eta }}{\rho }\frac{\overline{{\Omega }^{\prime }(\eta )}}{\left|{\Omega }^{\prime }(\eta )\right|}{J}_{n+1}(k\left|\Omega (\eta )\right|){\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^{n+1}]+A_n[\frac{\eta }{\rho }\frac{{\Omega }^{\prime }(\eta )}{\left|{\Omega }^{\prime }(\eta )\right|}{H}^{(1)}{}_{n-1}(k\left|\Omega (\eta )\right|){\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^{n-1}\\ -\frac{\overline{\eta }}{\rho }\frac{\overline{{\Omega }^{\prime }(\eta )}}{\left|{\Omega }^{\prime }(\eta )\right|}{H}^{(1)}{}_{n+1}(k\left|\Omega (\eta )\right|){\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^{n+1}]\}-e_{15}{\displaystyle \sum _{n=0}^{\infty }{B}_n}n{k}^{-n}\frac{\overline{\eta }}{\rho }\frac{\overline{{\Omega }^{\prime }(\eta )}}{\left|{\Omega }^{\prime }(\eta )\right|}{(\overline{\Omega (\eta ))}}^{-n-1}=0\\ D_{\rho }{|}_{\rho =a}=D_{\rho }{}^c{|}_{\rho =a}=-{\epsilon }_{11}\frac{\partial {\varphi }^c}{\partial r}{|}_{\rho =a}\\ {\epsilon }_{11}{\displaystyle \sum _{n=0}^{\infty }{B}_{n}n{k}^{-n}\frac{\overline{\eta }}{\rho }}\frac{\overline{{\Omega }^{\prime }(\eta )}}{\left|{\Omega }^{\prime }(\eta )\right|}{[\overline{\Omega (\eta )}]}^{-n-1}=-{\epsilon }_0{\displaystyle \sum _{n=0}^{\infty }{C}_{n}n{k}^n\frac{\eta }{\rho }}\frac{{\Omega }^{\prime }(\eta )}{\left|{\Omega }^{\prime }(\eta )\right|}{[\Omega (\eta )]}^{n-1}\\ {\varphi }^{(t)}{|}_{\rho =a}={\varphi }^c\\ \frac{e_{15}}{{\epsilon }_{11}}{\displaystyle \sum _{n=-\infty }^{\infty }[A_n{H}_n{}^{(1)}(k\left|\Omega (\eta )\right|)]}{\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^n+B_n{[k\left|\Omega (\eta )\right|]}^{-n}{\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^n\\ -{\displaystyle \sum _{n=0}^{\infty }{C}_n}{[k\left|\Omega (\eta )\right|]}^n{\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^n=\frac{e_{15}}{{\epsilon }_{11}}{\displaystyle \sum _{n=-\infty }^{\infty }{w}_0{\mathrm{i}}^n{J}_n(k\left|\Omega (\eta )\right|)}{\left\{\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}\right\}}^n\end{array}$$

According to the above derivation, the boundary conditions can be written as an infinite-dimensional system of equations.

$${\displaystyle \sum _{n=-\infty }^{\infty }{\mathit{{\rm E}}}_n{\mathit{{\rm X}}}_n^{}}=\mathit{{\rm E}}$$

(16)

where

$${\mathit{{\rm E}}}_n=\left[\begin{array}{ccc}{{\rm E}}_{11}^{}& {{\rm E}}_{11}^{}& {{\rm E}}_{11}^{}\\ {{\rm E}}_{21}^{}& {{\rm E}}_{22}^{}& {{\rm E}}_{23}^{}\\ {{\rm E}}_{31}^{}& {{\rm E}}_{32}^{}& {{\rm E}}_{33}^{}\end{array}\right]{\mathit{{\rm X}}}_n^{}=\left[\begin{array}{c}{A}_n\\ B_n\\ C_n\end{array}\right]\mathit{{\rm E}}=\left[\begin{array}{c}{{\rm E}}_1\\ {{\rm E}}_2\\ {{\rm E}}_3\end{array}\right]$$

(17)

Using the orthogonality of complex exponential functions, multiply both sides of the equation by $e^{-is\theta }(s=1,2,\dots ,3n)$.

$${\displaystyle \sum _{\mathrm{n}=-\infty }^{\infty }{\mathit{{\rm E}}}_{ns}{\mathit{{\rm X}}}_n={\mathit{{\rm E}}}_s}$$

(18)

where

$${\mathit{{\rm E}}}_n=\left[\begin{array}{ccc}{{\rm E}}_{11}^n& {{\rm E}}_{11}^n& {{\rm E}}_{11}^n\\ {{\rm E}}_{21}^n& {{\rm E}}_{22}^n& {{\rm E}}_{23}^n\\ {{\rm E}}_{31}^n& {{\rm E}}_{32}^n& {{\rm E}}_{33}^n\end{array}\right]\begin{array}{}\end{array}{\mathit{{\rm X}}}_n^j=\left[\begin{array}{c}{A}_{n1}\\ A_{n2}\\ B_n\end{array}\right]{\mathit{{\rm E}}}_{\mathrm{s}}=\left[\begin{array}{c}{{\rm E}}_1\\ {{\rm E}}_2\\ {{\rm E}}_3\end{array}\right]$$

(19)

According to Equation (18), we can derive the infinite system of linear equations for computing the mode coefficients $A_n,{{\rm B}}_n,C_n$, where $n=-\infty ~+\infty$.

6. Dynamic Stress-Concentration Factor

The dynamic stress concentration around the hole can be described by the Dynamic Stress-Concentration Factor (DSCF). The DSCF is the ratio of the hoop dynamic stress around the defect to the hoop stress amplitude in the incident direction of the incident wave [30].

$$DSCF=\left|\frac{{\tau }_{\theta z}}{{\tau }_0}\right|$$

(20)

where ${\tau }_0=w_0\chi k$ and

$${\tau }_{\theta z}=c_{44}\frac{1}{\mathrm{r}}\frac{\partial w}{\partial \theta }+e_{15}\frac{1}{\mathrm{r}}\frac{\partial \phi }{\partial \theta }$$

(21)

Then,

$$\begin{array}{cc}\hfill DSCF& =\frac{k}{2}{c}_{44}\mathrm{i}(1+\frac{e_{15}^2}{c_{44}{\epsilon }_{11}}){\displaystyle \sum _{n=-\infty }^{+\infty }\{\frac{\eta }{a}[w_0{\mathrm{i}}^n{J}_{n-1}(k\left|\Omega (\eta )\right|)}\hfill \\ & +A_n{H}_{n-1}^1(k\left|\Omega (\eta )\right|)]{[\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}]}^{n-1}+A_n{H}_{n+1}^1(k\left|\Omega (\eta )\right|)]{[\frac{\Omega (\eta )}{\left|\Omega (\eta )\right|}]}^{n+1}\hfill \\ & +\frac{\overline{\eta }}{a}[w_0{\mathrm{i}}^n{J}_{n+1}(k\left|\Omega (\eta )\right|)\}+e_{15}\mathrm{i}{\displaystyle \sum _{n=0}^{+\infty }\frac{\overline{\eta }}{a}n{B}_n{k}^{-n}}{\overline{\Omega (\eta )}}^{-(n+1)}\hfill \end{array}$$

(22)

7. Simulation of Numerical Examples and Discussion

According to the above derivation, we can calculate the DSCF around the regular polygonal hole on any piezoelectric ceramic under the condition of known piezoelectric ceramic-related parameters. However, the resulting DSCF forms are infinite. According to the characteristics of the Bessel function, as n increases, the coefficients ($A_n,{{\rm B}}_n,C_n$) all tend to 0. In the actual calculation, we can choose the appropriate minimum value of n according to the decision to truncate the DSCF. In order to check the correctness and usability of the derivation, we carried out a numerical simulation with a specific material and analyzed the results, which is presented below.

BaTiO3 (BT)-based piezoelectric ceramics are widely regarded as one of the candidates for lead-free piezoelectric ceramics due to their superior piezoelectricity. Wang et al. [31] studied the BT-based ceramics’ (1 − x)[(Ba_0.94Ca_0.06) (Ti_0.92Sn_0.08)]-xSm₂O₃-0.06 mol% GeO₂ (abbreviated as (1 − x)BCTS-xSm-0.06G) comprehensive electrical properties. They proposed that the material obtained optimized piezoelectric properties under the condition of 3 kv/mm (non-180° domain switching under high polarization electric field). Therefore, we selected (1 − x)BCTS-xSm-0.06G with a different doping ratio (x) under the condition of 3 kv/mm for numerical simulation, as shown in Figure 3.

It can be determined from the dynamic stress-concentration formula of Equation (22) that the dynamic stress-concentration coefficient is related to the wave number ($ka$) of the incident elastic wave, the piezoelectric constant (d₃₃) of the material and the mapping function (Ω(η)). By changing ka, we obtained the stress concentration around the regular n-sided hole on (1 − x)BCTS-xSm-0.06G with different doping amounts (i.e., different d₃₃), as shown in Figure 4 and Figure 5.

8. Results

In this paper, the dynamic stress concentration around regular n-sided holes in piezoelectric ceramics was studied. Firstly, decoupling was carried out by the auxiliary function method, and the form of analytical solution was obtained by wave function expansion. Then, the mode coefficients in the analytical solution were determined by the simplified boundary conditions obtained after conformal mapping and the orthogonality of the complex exponential function. Finally, the dynamic stress concentration coefficient around the hole could be obtained by truncation according to the required accuracy. We used (1 − x)BCTS-xSm-0.06G piezoelectric ceramics for numerical simulation to verify the feasibility of the method, and obtained the following conclusions:

• According to the material support, the piezoelectric constant e₁₅ of (1 − x)BCTS-xSm-0.06G under different values of x varies. When x is around 0.03, the piezoelectric constant e₁₅ reaches the peak. Selecting an appropriate value of x will effectively improve the piezoelectric properties of the material.
• Within the data range, the larger the piezoelectric constant e₁₅, the stronger the piezoelectric effect of the material, and the larger the dynamic stress concentration factor at the same position.
• When ka increases, the dynamic stress concentration around the defect fluctuates more violently, but the value decreases, and the dynamic stress concentration of materials with different piezoelectric constants e₁₅ is closer.
• The maximum value of the dynamic stress concentration coefficient of the regular polygon is obtained at its vertices. It can be seen that the dynamic stress concentration of the regular polygon is mainly significant at the vertices.
• The maximum value of the dynamic stress concentration factor of the regular m-gon decreases with the increase in m, and the speed of change is first fast and then slow. Since the increase of m leads to an increase of the vertices of the regular m-polygon, the dynamic stress concentration is more dispersed and moderate, and the maximum value of the dynamic stress concentration is also smaller.

The theoretical and numerical results presented in this paper are expected to be applied to the dynamic analysis and strong design of piezoelectric ceramic structures, and provide suggestions for the subsequent large-scale application and production of BCTS materials. By changing the piezoelectric material constant and the conformal transformation formula, the DSCF of any hole in any piezoelectric material can theoretically be obtained.