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Hindawi Publishing Corporation The Scientific World Journal Volume 2013, Article ID 854126, 9 pages http://dx.doi.org/10.1155/2013/854126

Research Article Torque for an Inertial Piezoelectric Rotary Motor Jichun Xing and Lizhong Xu Mechanical Engineering Institute, Yanshan University, Qinhuangdao 066004, China Correspondence should be addressed to Lizhong Xu; [email protected] Received 26 September 2013; Accepted 24 November 2013 Academic Editors: G. Carbone and O. D. Makinde Copyright © 2013 J. Xing and L. Xu. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited. For a novel inertial piezoelectric rotary motor, the equation of the strain energy in the piezoceramic bimorph and the equations of the strain energy and the kinetic energy in the rotor are given. Based on them, the dynamic equation of the motor is obtained. Using these equations, the inertial driving torque of the motor is investigated. The results show that the impulsive driving torque changes with changing peak voltage of the excitation signal, the piezoelectric stress constant, the thickness of the piezoceramic bimorph, and the rotor radius obviously. Tests about the motor torque are completed which verifies the theory analysis here in. The results can be used to design the operating performance of the motor.

1. Introduction Piezoelectric motors maintain relatively high torque at relatively low speeds, without a reduction gear [1, 2]. Among all of the piezoelectric motors, inertial drive principle has the advantage of simpler requirements to the construction and driving circuitry [3]. One type of the inertial motors is based on the impact drive mechanism from impulse inertial force [4]. Using the mechanism, the micromanipulator for cell manipulation and auxiliary positioning system for STM and AFM were developed [5, 6]. Another type of the inertial motors is based on the smooth impact drive mechanism. Here, a base plate or bar is driven with rapid expansion and slow shrinkage. The slider on the base slips during rapid motion and follows the base due to frictional force. With this principle, many applications were proposed and fabricated [7–9]. Choi et al. proposed a dynamic model to investigate dynamic characteristics of a novel type of inertial actuator and verified the model through comparison of voltage-dependent actuating forces between experiment and analysis [10]. Lipanov et al. proposed an inertial piezoelectric step drive for subnanosize-accuracy movements [11]. Gulyaev et al. used backlash-free screw-nut pairs in an inertial piezodrive to increase movement accuracy of an inertial piezoelectric drive [12]. Mazeika and Vasiljev proposed a novel design of tiny piezoelectric inertial motor based on inertial motion of the slider applying sticks and slip phases between stator and slider, and a prototype inertial

piezoelectric motor was built. The motor has simple design and consists of the slider with a bimorph piezoceramic disc and the clamped cylindrical shaft used for sliding [13]. However, these motors belong to the linear inertial piezoelectric motors and the inertial piezoelectric rotary motor was seldom reported. For further miniaturization of the rotational piezoelectric motors, the authors proposed a novel inertial piezoelectric rotary motor [14]. The motor structure is simple and further miniaturization of the rotational piezoelectric motor can be done easily. However, the inertial driving torque of the motor has not been investigated yet. It is unfavorable to design the loadcarrying ability of the motor. In this paper, the equations of the strain energy in the piezoceramic bimorph and the equations of the strain energy and the kinetic energy in the rotor are deduced. Based on them, the dynamic equation of the motor is obtained. Using these equations, the inertial driving torque of the motor is investigated. Tests about the relationship between the motor torque and the exciting voltage frequency or amplitude are done. The results are useful for design and control of the operating performance of the motor.

2. Voltage Excitation As shown in Figure 1, the novel inertial rotary motor consists of a stator and a rotor. The rotor includes an outer ring,

2

The Scientific World Journal Bolt

Housing

Needle

Adapting piece

Bolt

Piezoelectricity ceramic piece

·

Needle Vibrator

Wire Vibrator

Signal source

Base

Shaft Housing Adapting piece Base

Shaft Bearing

(a) Motor structure

(b) 3D model

Pzt

−

+

+

−

(c) Rotor structure and piezoceramic bimorph arrangement

Figure 1: Motor and rotor structures.

an inner ring, and two ribs connecting the outer ring to the inner ring. The inner ring is mounted on a supporting bearing and the outer ring is used as the inertial mass. The piezoceramic bimorph is adhered on each side surface of the two ribs. As soon as a rapid rise input voltage is supplied to the motor, it excites the transverse bending vibration of the two ribs. Thus, the inertial force within the outer ring occurs which causes inertial torque to be applied to the rotor and makes it rotate. Then, a slow decreasing input voltage is supplied to the motor, so the inertial forces within the outer ring are so small that the inertial torque can be balanced by the friction torque between the rotor and the bearing. Thus, the rotor does not rotate. The rapidly increasing and slowly decreasing input voltage with a special frequency is supplied to the motor periodically, and then the rotor can rotate continuously. For the motor motion, a saw-tooth-type electric signal is applied (see Figure 2). Here, 𝑡 is the time, 𝑇 is the period of the saw-tooth cycle, 𝜇 (0 < 𝜇 < 1) is the ratio of the rise time to the period, and 𝐴 is the amplitude of voltage signal 𝑉(𝑡). The voltage signal can be written by 𝐴 { { { 𝜇𝑇 𝑡 𝑉 (𝑡) = { 𝐴 𝐴 { { 𝑡+ 1−𝜇 { (𝜇 − 1) 𝑇

∞

𝑉 (𝑡) = 𝑎0 + ∑ [𝑎𝑛 cos (𝑛𝜔𝑡) + 𝑏𝑛 sin (𝑛𝜔𝑡)] ,

(2)

𝑛=1

where 𝑎0 = =

1 𝑇 ∫ 𝑉 (𝑡) 𝑑𝑡 𝑇 0 𝜇𝑇 𝑇 𝐴 𝐴 𝐴 1 𝑡+ (∫ 𝑡𝑑𝑡 + ∫ ( ) 𝑑𝑡) 𝑇 0 𝜇𝑇 1 −𝜇 (𝜇 − 1) 𝑇 𝜇𝑇

1 = 𝐴 2 𝑎𝑛 =

(3)

𝐴 (−1 + cos (2𝑛𝜇𝜋)) 2 𝑇 , ∫ 𝑉 (𝑡) cos (𝑛𝜔𝑡) 𝑑𝑡 = 𝑇 0 2𝑛2 𝜋2 𝜇 (1 − 𝜇)

𝑏𝑛 =

𝐴 sin (2𝑛𝜇𝜋) 2 𝑇 . ∫ 𝑉 (𝑡) sin (𝑛𝜔𝑡) 𝑑𝑡 = 2 2 𝑇 0 2𝑛 𝜋 𝜇 (1 − 𝜇)

3. The Impulsive Moment

(0 ≤ 𝑡 < 𝜇𝑇) (𝜇𝑇 ≤ 𝑡 ≤ 𝑇) .

The voltage signal can be written in the Fourier series as

(1)

The rotor of the motor can be considered as a beam with inertial mass at its two ends. Four piezoceramic bimorphs are

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3

V(t)

𝑙

𝑙 = ∫−𝑙 𝐸𝐼𝜙𝑖󸀠󸀠 (𝑥)𝜙𝑗󸀠󸀠 (𝑥)𝑑𝑥 and 𝑙 is the length of where 𝑘𝑖𝑗𝑙 = 𝑘𝑗𝑖 the rotor beam (see Figure 3). Four piezoceramic bimorphs are used in the motor, and then the total strain energy 𝑉 in the rotor and the piezoceramic bimorphs is

A

𝜇T T

0

t

𝑉 = 4𝑉𝑝 + 𝑉𝐿\𝑃 .

Figure 2: Applied electrical signal wave.

(8)

Kinetic energy 𝐸𝑚 of the rotor is y

Pzt

𝐸𝑚 = m

(9)

m

x l

2 𝜕𝑦 1 𝑙 1∞ ∞ ∫ 𝜌𝑆[ (𝑥, 𝑡)] 𝑑𝑥 = ∑ ∑ 𝑚𝑖𝑗 𝑞𝑖̇ (𝑡) 𝑞𝑗̇ (𝑡) , 2 −𝑙 𝜕𝑡 2 𝑖=1 𝑗=1

l

𝑙

where 𝑚𝑖𝑗 = 𝑚𝑗𝑖 = ∫−𝑙 𝜌𝑆𝜙𝑖 (𝑥)𝜙𝑗 (𝑥)𝑑𝑥 + 𝑚𝜙𝑖 (−𝑙)𝜙𝑗 (−𝑙) + 𝑚𝜙𝑖 (𝑙)𝜙𝑗 (𝑙) is the equivalent mass of the rotor and 𝑚 is the inertial mass. Substituting (8) and (9) into Lagrange equation yields

Figure 3: Dynamics model of the rotor.

adhered on side surface of the beam (see Figure 3). The strain in the piezoceramic bimorphs can be calculated as 𝜀1 =

2

ℎ 𝜕 𝑦 (𝑥, 𝑡) , 2 𝜕𝑥2

(4)

where 𝑦(𝑥, 𝑡) is the transverse displacement of the beam, 𝑥 is the length coordinate of the beam, ℎ is the thickness of the beam, and 𝜀1 is the strain in the piezoceramic bimorphs. By substituting (4) into the piezoelectric equation, the stress in the piezoceramic bimorph can be given [15] as ℎ 𝐸 𝜕2 𝑦 (𝑥, 𝑡) , 𝜎1 (𝑥, 𝑡) = −𝑒31 𝐸3 + 𝑐11 2 𝜕𝑥2

(5)

where 𝐸3 is the electric-field intensity on the piezoceramic bimorph, 𝐸3 = 𝑉(𝑡)/ℎ𝑝 , ℎ𝑝 is the thickness of the piezoce𝐸 is ramic bimorph, 𝑒31 is the piezoelectric stress constant, 𝑐11 the stiffness constant, and 𝜎1 (𝑥, 𝑡) is the stress in the piezoceramic bimorph. From (4) and (5), we know that the strain energy 𝑉𝑝 in the piezoceramic bimorph is 𝑉𝑝 = =

𝑏 𝑙𝑝 ∫ 𝜎 (𝑥, 𝑡) 𝜀1 𝑑𝑥 2 0 1

M𝑞 ̈ (𝑡) + C𝑞 ̇ (𝑡) + K = F (𝑡) ,

where M = [𝑚𝑖𝑗 ] is the mass matrix, K = [𝑘𝑖𝑗 ] is the stiffn𝑝 ess matrix, 𝑘𝑖𝑗 = 𝑘𝑖𝑗 + 𝑘𝑖𝑗𝑙 , F(𝑡) is the generalized force vec𝑙

tor, C = [𝑐𝑖𝑗 ] is the damping matrix, and 𝑐𝑖𝑗 = 𝑐𝑗𝑖 = ∫0 𝐶𝑑 𝜙𝑖 (𝑥)𝜙𝑗 (𝑥)𝑑𝑥; here the friction damping between stator and rotor is considered and the equivalent damping coefficients are determined from equal energy principle. Using the orthogonality of the mode functions, (10) can be changed into the following form uncoupled to each other: Mn 𝑞 ̈ (𝑡) + Cn 𝑞 ̇ (𝑡) + Kn 𝑞 (𝑡) = Fn (𝑡) ,

𝑙𝑝 1∞ 𝑝 𝑏ℎ ∞ ∑𝑞𝑖 (𝑡) ∫ −𝑒31 𝐸3 𝜙󸀠󸀠 (𝑥) 𝑑𝑥 + ∑𝑘𝑖𝑗 𝑞𝑖 (𝑡) 𝑞𝑗 (𝑡) , 4 𝑖=1 2 𝑖=1 0 (6) 𝑝

𝑝

𝜕2 𝑦 (𝑥, 𝑡) 1 𝑙 1∞ ∞ 𝑙 ] 𝑑𝑥 = ∑ ∑𝑘 𝑞 (𝑡) 𝑞𝑗 (𝑡) , ∫ 𝐸𝐼[ 2 0 𝜕𝑥2 2 𝑖=1 𝑗=1 𝑖𝑗 𝑖 (7)

𝑙 𝑏ℎ (2 ∫ 𝑒31 𝐸3 𝛿 (𝑥 − 𝑥𝑎 ) 𝜙𝑖󸀠󸀠 (𝑥) 𝑑𝑥 4 −𝑙 𝑙

+2 ∫ 𝑒31 𝐸3 𝛿 (𝑥 − 𝑥𝑏 ) 𝜙𝑖󸀠󸀠 (𝑥) 𝑑𝑥) −𝑙

=

𝑙𝑝

2

𝑉𝐿/𝑃 =

(11)

where Mn , Cn , and Kn are the diagonal mass, damping, and 𝑇 stiffness matrixes. Fn (𝑡) = {𝐹1 (𝑡) ⋅ ⋅ ⋅ 𝐹𝑖 (𝑡) ⋅ ⋅ ⋅} is the regular force vector. Each element 𝐹𝑖 (𝑡) of the regular force vector is 𝐹𝑖 (𝑡) =

2 𝐸 󸀠󸀠 where 𝑦(𝑥, 𝑡) = ∑∞ 𝑛=1 𝜙𝑛 (𝑥)𝑞𝑛 (𝑡), 𝑘𝑖𝑗 = 𝑘𝑗𝑖 = ∫0 (𝑏ℎ /4)𝑐11 𝜙𝑖 (𝑥)𝜙𝑗󸀠󸀠 (𝑥)𝑑𝑥, 𝜙𝑗 (𝑥) is the mode function, and 𝑙𝑝 and 𝑏 are the length and width of the piezoceramic bimorph, respectively. The strain energy 𝑉𝐿/𝑃 in the rotor beam is

(10)

(12)

𝑏ℎ𝑒31 𝑉 󸀠󸀠 (𝜙𝑖 (𝑥𝑎 ) + 𝜙𝑖󸀠󸀠 (𝑥𝑏 )) , 2ℎ𝑝

where 𝑥𝑎 and 𝑥𝑏 are the average positions of the piezoceramic bimorphs. The solution of (11) is 𝑞𝑗 =

𝑡 1 ∫ 𝐹𝑗 (𝜏) 𝑒−𝜉𝑗 𝜔𝑗 (𝑡−𝜏) sin 𝜔𝑟𝑗 (𝑡 − 𝜏) 𝑑𝜏. 𝑀𝑗 𝜔𝑟𝑗 0

(13)

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1 0 −1

0

0.5

×10

1 t (s)

1.5

15 10 5 0

×10−3

0

2

4

6

8

×10−4

6

8

×10−4

t (s)

−6

×10

−7

5

5

T (Nm)

T (Nm)

×10−7 y (m)

y (m)

×10−6 2

0 −5 0

0.5

1

1.5

×10−3

0 −5

2

0

4 t (s)

t (s) (a) 𝜔 = 10000 rad/s

(b) 𝜔 = 20000 rad/s

Figure 4: The displacement response and the corresponding impulsive moment.

{ ∞ { { 1 𝑎0 + ∑ { { 2 2 { 𝑛=1 √ 2 ) + (2𝜉 𝛾 ) (1 − 𝛾𝑛𝑗 𝑗 𝑛𝑗 { } } } × [𝑎𝑛 cos (𝑛𝜔𝑡 − 𝜑𝑛𝑗 ) + 𝑏𝑛 sin (𝑛𝜔𝑡 − 𝜑𝑛𝑗 )] } . } } } (14)

2 )). Here, 𝜑𝑛𝑗 = arctan(2𝜉𝑗 𝛾𝑛𝑗 /(1 − 𝛾𝑛𝑗 The steady response of the rotor to electric excitation is ∞

𝑦 (𝑥, 𝑡) = ∑ 𝜙𝑗 (𝑥) 𝑞𝑗 (𝑡) 𝑗=1 ∞

=∑ 𝑗=1

𝐹𝑛 𝜙𝑗 (𝑥) 𝑀𝑗 𝜔𝑗2

{ ∞ { √𝑎𝑛2 + 𝑏𝑛2 { × {𝑎0 + ∑ { 2 2 { 𝑛=1 √ 2 ) + (2𝜉 𝛾 ) (1 − 𝛾𝑛𝑗 𝑗 𝑛𝑗 { } } } 𝑏 × cos (𝑛𝜔𝑡 − 𝜑𝑛𝑗 − arctan ( 𝑛 )) } . } 𝑎𝑛 } } (15) ̇ 𝑡) and acceleration 𝑦(𝑥, ̈ 𝑡) of From (15), the velocity 𝑦(𝑥, the motor rotor can be given.

y (m)

𝐹𝑛 𝑞𝑗 = 𝑀𝑗 𝜔𝑗2

×10−6 15

3

10

2

5

1

0

0

0

0.5

1

2

1.5

2.5

3

(rad/s)

T (Nm)

×10−6 4

By substituting (2) and (12) into (13) and neglecting the transient solution, the steady solution can be obtained

−5 3.5 ×104

Displacement of the end Inertial moment of the end

Figure 5: The frequency response of the displacement and impulsive moment.

̈ 𝑡) and 𝑇(𝑡) = −𝐽ℎ 𝛼, the impulsive moment for From 𝑦(𝑥, the motor can be given as ∞

𝑇 (𝑡) = ∑ 𝑗=1

𝐽ℎ 𝐹𝑛 𝜙𝑗 (𝑙) 𝑙𝑀𝑗 𝜔𝑗2

∞

𝑛2 𝜔2

∑ 𝑛=1 √

2

2

2 ) + (2𝜉 𝛾 ) (1 − 𝛾𝑛𝑗 𝑗 𝑛𝑗

× [𝑎𝑛 cos (𝑛𝜔𝑡 − 𝜑𝑛𝑗 )

(16)

+𝑏𝑛 sin (𝑛𝜔𝑡 − 𝜑𝑛𝑗 )] , where 𝐽ℎ is the rotary inertia of the rotor, 𝛼 is the angular ̈ 𝑡)/𝑙. acceleration of the rotor end, and 𝛼 = 𝑦(𝑥,

5

×10−6

×10−6

1.5

6

1

4 T (Nm)

T (Nm)

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0.5

2

0

0

−0.5

−2 −4

−1 2

4

6

8

(rad/s)

10 ×104

2

4

6

8

10 ×104

8

10 ×104

(rad/s) 𝜇 = 0.7 𝜇 = 0.8 𝜇 = 0.9

𝜇 = 0.7 𝜇 = 0.8 𝜇 = 0.9 (a) Mode 1

(b) Mode 2

×10−6

×10

10

−6

6 4 T (Nm)

T (Nm)

5

0

2 0 −2

−5 4

2

6 (rad/s)

8

10 ×104

−4

2

4

6 (rad/s)

𝜇 = 0.7 𝜇 = 0.8 𝜇 = 0.9

𝜇 = 0.7 𝜇 = 0.8 𝜇 = 0.9 (c) Mode 3

(d) Mode 4

Figure 6: The response of the impulsive moment as a function of 𝜇.

4. Simulation and Test Equations in this paper are utilized for the impulsive moment analysis of the inertial piezoelectric rotary motor. The parameters of the numerical example are shown in Table 1. The displacement response of the rotor end to the excitation signals and the corresponding impulsive moment under the different exciting frequencies are given in Figure 4 (here, 𝜔 is the frequency of the excitation signals). From Figure 4, the following observations were worth noting. (1) Under the periodic voltage excitation with saw-tooth wave, the dynamic displacement at the end of the rotor changes periodically. The rise edge of the excitation voltage corresponds to multipeaks of the

Table 1: Parameters of the numerical example. 𝑅1 (mm) 12 𝑙𝑝 (mm) 10

𝑅2 (mm) 13 𝑏 (mm) 5

ℎ (mm) 1 ℎ𝑝 (mm) 0.5

𝑙 (mm) 12 𝑒31 (mm) −0.046

𝐸 (Gpa) 120 𝜌 (kg⋅m−3 ) 8.9 × 103

dynamic displacement which are different from each other, and its trailing edge corresponds to a large peak in an opposite direction. (2) Under the periodic voltage excitation with saw-tooth wave, the changes of the impulsive moment along

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12

×10−6 25

10

20

8

15

Mode 3

T (Nm)

T (Nm)

×10−5

6 4 2

Mode 3

10 5 0

0

−5

−2 2

4

6

8

(rad/s)

2

10 ×104

8

10 ×104

6

8

10 ×104

A = 30 A = 40 A = 50 (a) 𝜉 change

−6

(b) 𝐴 change

Mode 3

×10 15

10

−6

Mode 3

10 T (Nm)

T (Nm)

6 (rad/s)

𝜉 = 0.01 𝜉 = 0.08 𝜉 = 0.2 ×10 15

4

5

5

0 0 −5 −5 2

4

6 (rad/s)

8

10 ×104

e31 = 0.046 e31 = 0.015 e31 = 0.024

2

4 (rad/s)

hp = 0.5 mm hp = 0.8 mm hp = 1 mm (c) 𝑒31 change

(d) ℎ𝑝 change

Figure 7: Changes of the impulsive moment along with the system parameters.

with time are similar to those of the dynamic displacement at the end of the rotor. As the frequency of the excitation signal grows, the peak number of the impulsive moment drops for the rise edge of the excitation voltage. (3) The driving torque of the motor is equal to the integral of the impulsive moment at a given time range. The results show that the integral is not zero which means that a driving torque is produced. (4) At a given time range, the integral of the impulsive moment is different for the different voltage excitation frequency. So, the changes of the driving torque of

the motor along with the voltage excitation frequency should be investigated further. The frequency responses of the displacement at the rotor end and the corresponding impulsive moment are given in Figure 5 (here, 𝜇 = 0.7 and 𝜉 = 0.1). Figure 5 shows the following. (1) As the frequency of the voltage excitation is near onenth of the natural frequency, the peaks of the displacement at the rotor end and the corresponding impulsive moment occur. (2) As the frequency of the voltage excitation is near the natural frequency of the motor (𝑛 = 1), the peaks

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7

×10−4 20

T (Nm)

15 10 5 0

Figure 9: The prototype motor and its driving system. −5

5

10 (rad/s)

15

×104

Structure 1 Structure 2 Structure 3

Figure 8: Changes of the impulsive moment along with the motor sizes.

of both displacement at the rotor end and the corresponding impulsive moment are the maximum. (3) As the frequency of the voltage excitation is equal to one-nth of the natural frequency, the jumping from positive peak to negative peak occurs. This is not favorable to operation of the motor. The frequency of the voltage excitation should be taken as slightly smaller than one-nth of the natural frequency. Figure 6 shows the impulsive moment as a function of the ratio of the rise time to the period for the excitation voltage. It shows the following.

Table 2: Different motor sizes and exciting frequencies. Size 𝑅1 number (mm) 1 2 3

13 18 25

𝑅2 (mm)

𝑘 (mm)

𝑙 (mm)

ℎ (mm)

𝜔 (rad/s)

12 15 17.5

5 10 15

12 15 17.5

1 2 3

84254 161768 49336

moment is increased by more than 6 times. So, the small damping should be maintained to increase the driving torque of the motor. (2) As the peak voltage 𝐴 of the excitation signal grows, the impulsive moment of the motor grows. The impulsive moment increases nearly linearly with increasing the peak voltage 𝐴. (3) As the piezoelectric stress constant 𝑒31 grows, the impulsive moment of the motor grows. The impulsive moment increases nearly linearly with increasing the piezoelectric stress constant 𝑒31 as well. So, the piezoelectric material with larger constant 𝑒31 should be selected.

(1) As the ratio of the rise time to the period for the excitation voltage grows, the peak of the impulsive moment grows. The effects of the 𝜇 value on the positive impulsive moment peak are relatively small, and its effects on the negative impulsive moment peak are relatively large.

(4) As the thickness ℎ𝑝 of the piezoceramic bimorph grows, the impulsive moment of the motor grows. So, larger thickness ℎ𝑝 of the piezoceramic bimorph should be taken.

(2) For the different modes, the impulsive moment peaks are different from each other at the same 𝜇. For mode 3, the impulsive moment peak is the maximum. It shows that mode 3 is the most favorable for the motor operation.

(5) As the motor size grows, the impulsive moment of the motor grows obviously. It is because the rotary inertia of the motor grows obviously with increasing the motor size. Hence, the design of the motor size should be done according to load-carrying requirement.

Changes of the impulsive moment along with the system parameters are investigated (see Figure 7). Changes of the impulsive moment along with the motor sizes are given in Figure 8. Table 2 shows three different motor sizes and corresponding exciting frequencies. Here, only the results for mode 3 are given. They show the following.

Tests are done on the inertial rotary motor to obtain the relationship between the motor torque or speed and the exciting voltage frequency or amplitude. The motor was driven by a signal generator (YB-1602) and a power amplifier (HFVA-42). Here, the saw-tooth wave voltage signals were used (𝜇 = 0.9). The prototype motor and its driving system are given in Figure 9. The experimental results are given in Figure 10. The comparison between the experimental results and the calculated values is given in Table 3. They show the following.

(1) As the damping coefficient 𝜉 drops, the impulsive moment of the motor grows. When the damping coefficient 𝜉 is reduced to one-eighth, the impulsive

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120 50 100 Speed (r/min)

Speed (r/min)

40 30 20

80 60 40

10

20

0 6200

6250 6300 Frequence (Hz)

0

6350

40

(a) 𝜔 changes 𝑉 = 100 V

60

80

100 120 Voltage (V)

140

160

140

160

(b) 𝜔 = 6310 Hz 𝑉 changes

0.35

0.5

0.3 0.25

Torque (Nmm)

Torque (Nmm)

0.4

0.2 0.15

0.3

0.2

0.1 0.1 6280

6290

6300 6310 Frequence (Hz)

6320

6330

40

60

80

100

120

Voltage (V)

(c) 𝜔 changes 𝑉 = 100 V

(d) 𝜔 = 6310 Hz 𝑉 changes

Figure 10: Changes of the motor speed and torque along with exciting frequency and voltage.

Table 3: Comparison of experimental results and theoretical values. Signal voltage (V) 75 100 125 150 175

Calculated maximum torque (Nmm)

Calculated average torque (Nmm)

Measured torque (Nmm)

Relative errors (%)

0.98 1.31 1.7 2.01 2.3

0.37 0.50 0.62 0.75 0.87

0.24 0.35 0.39 0.44 0.52

35 30 37 41 40

(1) As the peak of the voltage signal is 100 V, the model motor starts to rotate at 𝜔 = 6280 Hz. As the exciting frequency grows, the rotating speed of the motor increases significantly. It gets to the maximum value (59.6 rpm) at 𝜔 = 6310 Hz. As the exciting frequency further grows, the rotating speed of the motor decreases quickly. It stops to rotate at 𝜔 = 6330 Hz.

(2) For 𝜔 = 6310 Hz, the motor starts to rotate at 𝑉 = 25 V. The rotating speed of the motor grows nearly linearly with increasing the amplitude of the exciting voltage (from 25 V to 170 V). (3) The above results are obtained under the condition without the outer load. Here, the motor only bears the friction force within the motor. Under the outer load and 𝑉 = 100 V, the output torque of the motor increases significantly with increasing the exciting frequency. It gets to the maximum value (0.35 Nmm) at 𝜔 = 6310 Hz. As the exciting frequency further grows, the torque of the motor decreases quickly. The torque is zero at 𝜔 = 6330 Hz. (4) For 𝜔 = 6310 Hz, The output torque of the motor grows obviously with increasing the amplitude of the exciting voltage. At 𝑉 = 175 V, the output torque of the motor is 0.52 Mmm. (5) For 𝜔 = 6310 Hz and 𝑉 = 75–175 V, the relative errors between the measured torque and the calculated

The Scientific World Journal average torque are about 30–40%. It shows that the theory analysis results in this paper are believable.

5. Conclusions In this paper, the dynamic equation of the inertial piezoelectric rotary motor is obtained. The inertial driving torque of the motor is analyzed and tested. The results show the following. (1) The jumping from positive peak to negative peak occurs when the frequency of the voltage excitation is equal to the natural frequency which is not favorable for the motor. So, the frequency of the voltage excitation should be taken as slightly smaller than the natural frequency. (2) The impulsive driving torque changes with changing the system parameters. Larger peak voltage of the excitation signal, larger piezoelectric stress constant, larger thickness of the piezoceramic bimorph, and larger radius of the rotor can give larger impulsive driving torque. (3) The experimental output torque verifies the theory analysis here in.

Acknowledgment This project is supported by the National Natural Science Foundation of China (51275441).

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