Dynamic Characteristic Analysis of Tri-Stable Piezoelectric Energy Harvester with Double Elastic Amplifiers
Abstract:
In order to further improve the vibration energy harvesting efficiency of piezoelectric energy harvester under low frequency environmental excitation, this paper, based on the traditional magnetic tri-stable piezoelectric energy collector model, proposes a tri-stable piezoelectric energy harvester (TPEH+DEM) model with two elastic amplifiers which are installed between the U-shaped frame and the base and between the fixed end of the piezoelectric cantilever beam and the U-shaped frame respectively. Based on Hamilton principle, the motion equation of electromechanical coupling of TPEH+DEM system is established, and the analytical solutions of displacement, output voltage and power of the system are obtained by harmonic balance method. The effects of the mass of elastic amplifier, spring stiffness, magnet spacing and load resistance on the dynamic characteristics of energy harvesting of TPEH+DEM system are analyzed. The result shows that there are two peaks in the response output power of TPEH+DEM system in the operating frequency range. By adjusting the mass and stiffness of the elastic amplifier reasonably, the system can move into the inter-well motion under low external excitation intensity, and produce high output power. Compared with the traditional model which only has an elastic amplifier on the base of piezoelectric energy harvester, TPEH+DEM model has better energy harvesting performance under low frequency and low intensity external excitation.
1. Introduction
Piezoelectric energy harvester can convert mechanical energy in the environment into electrical energy by using piezoelectric effect to supply power to microelectronic devices. The early linear piezoelectric energy harvester has a narrow working frequency band, so it is difficult to effectively match with the broadband vibration frequency in the environment, which leads to low energy harvesting efficiency [1], [2], [3], [4], [5], [6], [7], [8]. To solve this problem, scholars at home and abroad begin to study the multi-stable piezoelectric energy harvester model to improve the energy harvesting performance of the system [9], [10], [11], [12], [13], [14], [15], [16]. Chen et al. [17], based on the bi-stable piezoelectric energy harvesting model, analyzed the effects of material parameters, frequency and amplitude of external excitation on the system performance. Kim and Seok [18] studied a magnetic tri-stable piezoelectric cantilever beam energy harvester, and described in detail the advantages of tri-stable piezoelectric energy harvester for broadband vibration energy harvesting under low intensity excitation. Zhou et al. [19], based on the magnetic tri-stable piezoelectric energy harvester model, used numerical simulation and experimental method to demonstrate that the tri-stable piezoelectric energy harvester has better energy harvesting effect than bi-stable energy harvester under low external excitation level. Zhou and Zuo [20] obtained the analytical expression of steady-state response of asymmetric tri-stable piezoelectric cantilever beam by harmonic balance method, and analyzed the influence of potential well depth on energy harvesting effect under different excitation conditions.
At present, most of the studied multi-stable piezoelectric energy harvesters are fixed on rigid bases. Once the positions of cantilever beams and magnets are fixed, it will be difficult to adjust the frequency bandwidth of piezoelectric harvesters to match the external excitation frequency by changing the relative positions between magnets, so as to realize large-scale inter-well motion [21], [22]. Considering the above shortcomings of rigid base and to further improve the power output of multi-stable piezoelectric energy harvester under weak excitation intensity, researchers introduce elastic amplifier base into the structure of multi-stable piezoelectric energy harvester [23]. Liu et al. [24] proposed an elastic amplifier piezoelectric energy harvester with added mass, and demonstrated through experiments that the energy harvester can enhance vibration harvesting and reduce resonance frequency while broadening its operating frequency range. Wang et al. [25] demonstrated through numerical simulation and experimental method that the bi-stable piezoelectric energy harvester (BPEH+EM) system with elastic amplifier is easier to jump out of the barrier and move into large-scale inter-well motion at lower excitation level, and produces higher output power. Wang et al. [26] designed a piezoelectric cantilever beam energy harvester model with elastic amplifier, which provides enough kinetic energy to overcome the tri-stable potential well barrier, so that the system moves into large-scale well motion.
Based on the magnetic tri-stable piezoelectric cantilever beam energy harvester model with elastic amplifier base, a new type of amplifier composed of mass block M_{f }and spring k_{f} is added to the fixed end of the piezoelectric cantilever beam to form a TPEH+DEM model with double elastic amplifiers. Considering the eccentric distance and moment of inertia of the free end magnet of the beam, the motion control equation of electromechanical coupling of TPEH+DEM system is established based on Hamilton principle, and the analytical solution of the equation is obtained by using harmonic balance method. Focus is put on the effects of the relative position of magnet spacing, the mass and stiffness of elastic amplifier on the energy harvesting performance of TPEH+DEM system, and the calculation result of TPEH+DEM model is compared with that of traditional TPEH+EM model.
2. Modeling of Piezoelectric Energy Harvester
Figure 1 is a structural model of the TPEH+DEM with double elastic amplifiers established in this paper. TPEH consists of a cantilever piezoelectric beam of length l and width b and a beam-end magnet (expressed by A) and two external magnets (expressed by B and C) fixed to the right side of the U-shaped frame. The horizontal distance between the piezoelectric beam cantilever end magnet A and the U-shaped frame fixed magnet is d_{h}, and the vertical distance from the free end magnet of the beam to the external magnet B (external magnet C) is d_{v}. The cantilever beam consists of a metal substrate with a thickness of h_{s} and two piezoelectric patches with a thickness of t_{p} covering the upper and lower surfaces of the cantilever beam. The two piezoelectric patches have opposite polarization in the thickness direction and are connected in series with an external load resistor R. DEM consists of two elastic amplifiers (denoted EM_{1} and EM_{2}), of which EM_{1 }comprises a U-shaped frame and a spring k_{b} between TPEH and the substrate; EM_{2 }consists of a spring k_{f }connecting the beam end mass M_{f }and the bottom of the U-shaped frame.
In Figure 1, z(s, t), z_{m}(t) and z_{b}(t) represent the relative vertical displacement between a certain point on the section of piezoelectric cantilever beam and the fixed end of the beam, the vibration displacement of the U-shaped frame and the vertical vibration displacement of the base, respectively. The eccentric distance of the beam-end magnet is represented by e. Assuming that the metal substrate and the piezoelectric layer are completely tightly bonded, the constitutive relation is expressed as follows:
where, parameters related to the substrate are denoted by superscript s, and parameters related to the piezoelectric layer are denoted by subscript p; x and y directions are represented by 1 and 3 in subscripts, respectively; T, S, Y, D_{3} and d_{31} denote the stress, strain, Young modulus, electric displacement, and piezoelectric constant of the piezoelectric cantilever beam, respectively; $\varepsilon_{33}^T$ is the dielectric constant of the piezoelectric layer when the stress is constant; E_{3}=-V(t)/(2t_{P}), E represents electric field strength and V(t) is voltage; the expression of the relationship between displacement and strain is $S_1^s=S_1^p=-y z^{\prime \prime}$, where y is the distance between the neutral axis of the piezoelectric cantilever beam and any point on its cross section, z^{″} is the curvature of the piezoelectric cantilever beam.
The Lagrange equation of the system is as follows:
where, T_{k} is kinetic energy, U_{e} is strain energy, W_{p} is electric potential energy of electric field, U_{m} is magnetic potential energy between magnets, U_{d} is elastic potential energy, and W is external work. Their expressions are as follows.
where, z(l, t) is the displacement of the piezoelectric cantilever beam at s=l; m=2ρ_{p}t_{p}b+ρ_{s}h_{s}b is the equivalent mass on the unit beam, where ρ_{p} is the density of the piezoelectric layer and ρ_{s} is the density of the substrate; the mass, eccentric distance and moment of inertia of free end magnet A of the piezoelectric cantilever beam are represented by M_{t}, e and J, respectively; (˙) denotes the derivative of time t.
where,
where, $\varepsilon_{33}^S=\varepsilon_{33}^T-d_{31}^2 Y_p$, $\varepsilon_{33}^S$ is the dielectric constant of the piezoelectric layer when the stress is constant.
According to the magnetic dipole model [27, 28] after considering eccentric distance at the free end magnet of the beam, it can be obtained that:
where, μ_{0}=4π×10^{-7}H⋅m^{-1} indicates vacuum magnetic conductivity,
$\mathbf{r}_{\mathrm{BA}}=\left[\begin{array}{ll}-d_{\mathrm{h}}-\Delta x & v(l, t)+e \sin \beta-d_{\mathrm{v} 1}\end{array}\right]$ ,
$\mathbf{r}_{\mathrm{CA}}=\left[\begin{array}{ll}-d_{\mathrm{h}}-\Delta x & v(l, t)+e \sin \beta+d_{\mathrm{v} 2}\end{array}\right]$ ,
The magnetic dipole moments are m_{A}=[M_{A}V_{A}cosβ M_{A}V_{A}sinβ], m_{B}=[-M_{B}V_{B} 0] and m_{C}=[-M_{C}V_{C} 0]. In Δx≈e(1-cosβ), β=arctanv^{'}(l), M_{A}, M_{B} and M_{C} are the magnetization intensity of magnets A, B and C, respectively, and V_{A}, V_{B} and V_{C} are the volumes of magnets A, B and C, respectively.
Using Galerkin method, the displacement z(s, t) is expressed as:
where, X_{r}(t) is the r-th modal coordinate of the piezoelectric cantilever beam, ϕ_{r}(s) represents the r-th modal function of the beam, and its normalized condition expression is:
where, δ_{rs} is the Kronecker function. When s=r, $\delta_{r s}$ is 1; when $s \neq r$, $\delta_{r s}$ is 0. The expression of inherent frequency of the piezoelectric cantilever beam under undamped vibration is $\omega_r=\lambda_r^2 \sqrt{Y I /\left(m l^4\right)}$, where λ_{r} is its eigen value. The calculation method of λ_{r} and vibration mode function can be seen in reference [18].
Considering only the first-order mode and substituting formula (10) into formula (9), this paper expands at X_{1}(t)=0 by using Taylor’s formula and can obtain:
where,
$k_0=\frac{2 k q_1}{\left(d_h^2+d_v^2\right)^2}$,
$\begin{aligned} & k_1=\frac{4 k}{\left(d_h{ }^2+d_v{ }^2\right)^{5 / 2}}\left[q_1\left(2.5 q_2-17.5 q_3{ }^2\right)\right. \\ & \left.-5 q_3 q_4\left(d_h{ }^2+d_v{ }^2\right)-q_5\right]\end{aligned}$
$\begin{aligned} & k_2=\frac{8 k}{\left(d_h^2+d_v^2\right)^{5 / 2}}\left[q_1\left(-2.5 q_6-17.5 q_3 q_7\right.\right. \\ & \left.+4.38 q_2{ }^2-78.75 q_2 q_3{ }^2+144.375 q_3{ }^4\right) \\ & +q_4\left(-2.5 q_7-17.5 q_2 q_3+52.5 q_3{ }^3\left(d_h{ }^2+d_v{ }^2\right)\right. \\ & \left.q_5\left(-2.5 q_2+17.5 q_3{ }^2\right)+5 q_3 q_8+q_9\right]\end{aligned}$
$\begin{aligned} & k_3=\frac{12 k}{\left(d_h{ }^2+d_v{ }^2\right)^{5 / 2}}\left[q_1\left(-2.5 q_{10}+13.125 q_3 q_{11}+8.75 q_2 q_6\right.\right. \\ & +4.375 q_7{ }^2-78.78 q_3{ }^2 q_6+78.25 q_2 q_3 q_7-288.75 q_3{ }^3 q_7 \\ & \left.+216.55 q_2{ }^2 q_3{ }^2-6.56 q_2{ }^3-938.44 q_2 q_3{ }^4+938.44 q_3{ }^6\right) \\ & +q_4\left(1.875 q_{11}-17.5 q_3 q_6+8.75 q_2 q_7-78.75 q_3{ }^2 q_7+\right. \\ & \left.39.38 q_2{ }^2 q_3-288.75 q_2 q_3{ }^2+375.375 q_3{ }^5\right)+q_5\left(-2.5 q_6\right. \\ & \left.-17.5 q_3 q_7+4.375 q_2{ }^2-78.75 q_2 q_3{ }^2+144.375 q_3{ }^4\right) \\ & +q_8\left(-2.5 q_7-17.5 q_2 q_3+52.5 q_3{ }^2\right)+q_9\left(-2.5 q_2+17.5 q_3{ }^2\right) \\ & \left.+5 q_3 q_{12}+q_{13}\right]\end{aligned}$
Coefficient κ, the expression of q_{i}_{=1…26} is shown in the previous reference [18].
Considering only the first-order mode, formula (2) is substituted into the Lagrange variational equation shown in formula (14):
where, $F(t)=-2 \xi_1 \omega_1 \dot{\eta}_1(t)$ is the generalized dissipative force of TPEH+DEM system, ω_{1} is the first-order natural frequency of the system, ξ_{1} is its damping ratio and Q(t) is generalized output charge. $\dot{Q}(t)=-V(t) / R$, where R represents the load resistance of external circuit. Through formula (14), the differential equation of motion of TPEH+DEM system can be obtained as follows:
where,
$\begin{gathered}M_0=m \int_o^l \phi_1(s) d s+M_t \phi_1(l)+M_t e \phi_1^{\prime}(l) \\ +M_{\mathrm{f}} \phi_1(0),\, M_1=m l+M_t+M_f+M_m, \\ \omega_1^2=Y I \int_0^l \phi_1^{\prime \prime}(s)^2 d s+k_f \phi_1(0)^2, \,\theta_1=Y_P b d_{31}\left(h+\frac{t_P}{2}\right) \int_0^l \phi_1^{\prime \prime}(s) d s, \,C_P=\frac{b l \varepsilon_{33}^s}{2 t_P} .\end{gathered}$
where,
$\begin{gathered}\omega_1^2=Y I \int_0^l \varphi_1^{\prime \prime} d s,\, g_0=m g \int_0^l \varphi_1(s) d s \\ +M_t g \varphi_1(l), \,\Gamma_1=m \int_0^l \varphi_1(s) d s+M_{\mathrm{t}}\left(\varphi_1(l)+e \varphi_1^{\prime}(l)\right) \\ \theta_1=Y_P b d_{31}\left(h+\frac{t_P}{2}\right) \int_0^l \varphi_1(s) d s, C_P=\frac{b l \varepsilon_{33}^S}{2 t_P} .\end{gathered}$
External excitation is set to $\ddot{v}_b(t)=\bar{v}_b \cos \left(\omega_e t\right)$, where $\bar{v}_b$ is the amplitude of external excitation, $\omega_{\mathrm{e}}$ is the circular frequency of excitation. Substituting dimensionless transformation $x=\eta_1 / l$, $\bar{V}=V C_p /\left(l \theta_1\right)$ and $\tau=\omega_1 t$ into formula (15), we can get
where, $K_b=\frac{k_b}{\omega_1^2}, K_1=\frac{k_1}{\omega_1^2}, K_2=\frac{k_2 l^2}{\omega_1^2}, \quad \Theta=\frac{\theta_1^2}{C_P \omega_1^2}, \alpha=\frac{1}{C_P R_L \omega_1}, F=-\frac{M_0 \bar{z}_b}{\omega_1^2 l}$.
The first and second equations of formula (16) are used to eliminate the variable V_{m}, and formula (16) is simplified to
3. Solution by Harmonic Balance Method
It is assumed that the solution of formula (17) can be expressed as:
where A, B, C and D are uncertain coefficients, the displacement amplitude of the piezoelectric cantilever beam can be expressed as $a=\sqrt{A^2+B^2}$, and the output voltage amplitude can be expressed as $u=\sqrt{C^2+D^2}$. We substitute formula (18) into formula (17), take the constant terms on both sides, and the coefficients of cos(ωτ) and sin(ωτ) are equal, and ignore the higher-order harmonic term, then the following equation is obtained:
where,
$\begin{gathered}\Pi_1=\frac{K_1 M_1+K_b}{K_b} \\ \Pi_2=\frac{2 \xi_1 M_1}{K_b} \omega^3-2 \xi_1 \omega, \\ \Pi_3=\frac{M_1-M_0^2}{K_b} \omega^4-\frac{\left(1-K_1\right) M_1+K_b}{K_b} \omega^2+1-K_1 \\ +\frac{3}{4} K_2 a^2+\frac{5}{8} K_3 a^4-\frac{3}{4} \frac{K_2 M_1}{K_b} \omega^2 a^2-\frac{5}{8} \frac{K_3 M_1}{K_b} \omega^4 a^4 \\ \Pi_4=\frac{\Theta M_1}{K_b} \omega^2-\Theta\end{gathered}$
In the steady state, all derivatives of time are 0. Therefore, the analytical expressions of displacement amplitude and voltage amplitude of the system can be obtained by using formulas (19-22) as follows:
The steady-state displacement amplitude a of TPEH+DEM system can be calculated by formula (23). The expressions of steady-state output voltage and power amplitude are:
4. Analysis of Calculation Result
In this chapter, focus will be put on the effects of relative position of magnets, load resistance, mass of elastic amplifier and spring stiffness ratio on the performance of TPEH+DEM (Table 1). The main physical and geometric parameters of the system are as follows [1].
Parameter | Value |
Length l | 75mm |
Width b | 20mm |
Thickness h_{s} | 0.2mm |
Piezoelectric modulus Y_{s} | 70Gpa |
Piezoelectric modulus Y_{p} | 60.98Gpa |
Density $\rho_s$ | 2700kg/mm^{3} |
Density $\rho_p$ | 7750kg/mm^{3} |
Piezoelectric constant d_{31} | -1.7×10^{-10}C/N |
Permittivity of free space $\varepsilon_{33}^s$ | 1.33×10^{-8}F/m |
Damping ratio $\xi_1$ | 0.01 |
Magnetization of magnets (A,B,C) | 1×10^{-6}m^{3} |
Volume of magnet (A,B,C) | 1.22×10^{-6}m^{3} |
Eccentricity e | 5mm |
Mass of tip magnet M_{t} | 14.9g |
We take M_{m}=60 g, d_{h}=21 mm, d_{v}=8 mm and k_{b}=8,000 N/mm. The variation curves of displacement and output power amplitudes of the two models of piezoelectric energy harvester models (TPEH+DEM, TPEH+EM) with excitation frequency are shown in Figure 2 and Figure 3, respectively. TPEH+EM is equipped with only an elastic amplifier, i.e. a spring k_{b }located between TPEH and the substrate.
We take M_{m}=60 g, d_{h}=21 mm, d_{v}=8 mm, k_{f}=50,000 N/mm and k_{b}=8,000 N/mm. Figure 4 and Figure 5 show the variation curves of displacement amplitude a and power amplitude P of TPEH+DEM system with excitation frequency in different values of M_{f} s, respectively. As can be seen from Figure 4 and Figure 5, with the increase of M_{f}, left displacement and power peak of the system increase continuously, while right displacement and power peak change little, but the frequency band range moves to the low frequency band.
Figure 6 and Figure 7 show the variation curves of left and right peak power of TPEH+DEM system with load resistance R in different values of M_{f} when M_{m}=60 g, d_{v}=8 mm, d_{h}=21 mm, k_{f}=50,000 N/mm and k_{b}=8,000 N/mm. It can be seen from Figure 6 that with the increase of R, left peak power of the system increases rapidly first, and the first local maximum P_{max1} appears, corresponding to the load resistance R_{opt1}, and then continues to increase after greatly decreasing (when the load resistance is R_{opt2}, it reaches the second local maximum P_{max2 }of the curve, and finally decreases gradually). In addition, it can be seen from Figure 6 that under the same M_{f}, the two local maxima are very close, and increasing M_{f} can obviously improve P_{max1} and P_{max2}. As shown in Figure 7, when M_{f} = 0.02g, left peak power of the system is 0.1130 W; when M_{f} increases to 0.06 g, right peak power of the system is 0.1115 W, that is, with the change of M_{f}, the peak power changes little.
We take M_{f}=60 g, M_{m}=60 g, k_{f}=50,000 N/mm and k_{b}=8,000 N/mm. Figure 8 and Figure 9 show the variation curves of left and right peak power of TPEH+DEM system corresponding to different relative positions between magnets with load resistance R. As can be seen from Figure 8, the variation trend of left peak power of the system with load resistance R is the same as that of Figure 6, and the peak power of the system corresponding to different d_{v} and d_{h} is relatively close. Figure 9 shows that the peak power of the system can be significantly increased by increasing d_{h} while keeping dv constant. However, when d_{h }is kept constant, the peak power decreases slightly with the increase of d_{v}.
We take k_{f}=50,000 N/mm, k_{b}=8,000 N/mm, d_{v}=8 mm and d_{h}=21 mm. Figure 10 and Figure 11 show the variation curves of steady-state voltage amplitude u with excitation acceleration when w is 0.8 and 1.2 respectively, and the mass of elastic amplifier is taken for different values. As can be seen from Figure 10 and Figure 11, each working condition corresponds to an excitation acceleration threshold, which enables the system to move into large-scale inter-well motion and generate high output voltage. When w is the same, the threshold of excitation acceleration required for the system to move into inter-well motion can be reduced by increasing the mass M_{f }and M_{m} of two elastic amplifiers, but the change of output voltage is not obvious. When the mass of elastic amplifiers is constant, the threshold of excitation acceleration increases with the increase of excitation frequency.
Taking the load resistance R=300 kΩ, as shown in Figure 12 and Figure 13, the steady-state voltage amplitude u of TPEH+DEM system varies with the excitation amplitude when the excitation acceleration w is 0.6 and 1.2, respectively and k_{f}/k_{b} is in different values. As shown in Figure 12 and Figure 13, when w=0.6, with the increase of k_{f}/k_{b}, the excitation threshold of the system decreases, while the steady-state voltage amplitude u changes little. When w is increased to 1.2, the excitation threshold obviously decreases with the increase of k_{f}/k_{b}, and the output voltage amplitude increases with the increase of k_{f}/k_{b }after moving into inter-well motion. It can be seen that when the excitation frequency is high, increasing the k_{f}/k_{b }value can make the system move into inter-well motion and produce higher output voltage at lower excitation intensity.
Figure 14 and Figure 15 show the variation curves of power and displacement amplitudes of the system when M_{m }is different in values and when R=300 kΩ, M_{f}=60 g, d_{h}=21, d_{v}=8, k_{f}=50,000 N/mm and k_{b}=50,000 N/mm. The result shows that, with the increase of excitation frequency, the power and displacement amplitudes of the system increase significantly at first, then decrease sharply after reaching the maximum value rapidly, then increase again, and then decrease after reaching the second local peak value when M_{m }keeps constant. In addition, with the increase of M_{m}, the peak power and displacement of the system increase significantly, and can enter the secondary ascending section at lower excitation frequency, resulting in higher local peak power.
5. Conclusion
(1) Based on Hamilton variational principle, the differential equation of motion of a tri-stable piezoelectric energy harvesting system with double elastic amplifiers is derived, and the analytical solution of electromechanical coupling equation describing the energy output characteristics of the system is obtained by using the harmonic balance method.
(2) With the increase of excitation frequency, the output power amplitude of TPEH+DEM system can produce two high and low peaks. Compared with TPEH+EM system, TPEH+DEM system has better energy harvesting performance under low frequency external excitation.
(3) At the same excitation frequency, the excitation acceleration threshold required for TPEH+DEM system to move into inter-well motion can be reduced by increasing the mass of elastic amplifiers; when the excitation frequency is high, increasing the stiffness ratio k_{f}/k_{b }of the two elastic amplifiers can make TPEH+DEM system move into inter-well motion at lower excitation intensity and produce higher output voltage.
(4) Increasing M_{m }can significantly improve the maximum peak power of TPEH+DEM system, and can make the system enter the secondary ascending section at lower excitation frequency, resulting in higher local peak power.
The data used to support the findings of this study are available from the corresponding author upon request.
The authors declare that they have no conflicts of interest.