Shock and Vibration

Shock and Vibration / 2021 / Article

Research Article | Open Access

Volume 2021 |Article ID 9911135 | https://doi.org/10.1155/2021/9911135

Semen Kopylov, Zhaobo Chen, Mohamed A. A. Abdelkareem, "Frequency-Based Control Strategy for Compact Electromagnetic Tuned Mass Damper", Shock and Vibration, vol. 2021, Article ID 9911135, 11 pages, 2021. https://doi.org/10.1155/2021/9911135

Frequency-Based Control Strategy for Compact Electromagnetic Tuned Mass Damper

Academic Editor: Marcos Silveira
Received22 Mar 2021
Revised10 Apr 2021
Accepted26 Apr 2021
Published04 May 2021

Abstract

The control of harmonic machine-induced vibration has been a common task in the engineering scope. The passive tuned mass dampers represent the most reliable and practical approach to reduce such excessive vibration. Additionally, different control strategies can be implemented on TMDs to improve the attenuation performance further. However, most of the proposed control strategies for TMDs represent cost and complex systems with many sensors, which hinders the broad implementation. In this paper, the frequency-based semiactive control (FBC) strategy was proposed for an electromagnetic tuned mass damper (ETMD). The concept of a controllable system with switched transistor was utilized for the proposed control strategy. The proposed control policy's effectiveness was validated by experimental results, where the controlled ETMD was applied on a protected mass test bench. This paper concluded that the proposed control strategy has a significant advantage over the passive TMD. The reduction of 14% of the excessive harmonic vibration for the protected structure was observed.

1. Introduction

Undesirable machine-induced vibrations with a harmonic nature can cause serious damage to mechanisms and structures. That kind of vibration can be induced by rotating machinery such as engines, driveshafts, flywheels, and rotors. As passive vibration absorption devices are limited to a specific narrow operation frequency bandwidth to reduce the unwanted influence of machine-induced vibrations, different control techniques under harmonic-based vibrations have been proposed, implemented, and investigated over decades. Takamoto et al. [1] proposed a new method by integrating model predictive and semiactive controls, and such a control strategy is known as predictive switching based on harmonic input (PSHI). The PSHI predicted the system’s future states by assuming the harmonic control inputs and harmonic disturbances that caused resonance. Wang [2] developed an active restricted control for harmonic vibration suppression. The study case demonstrated the feasibility of the proposed approach. Such control allows the reduction of vibration for systems where the numbers of sensors and actuators are limited. Harmonic vibrations induced by the unbalanced rotor of a magnetically suspended flywheel represent a challenge for control engineers. To suppress the harmonic vibrations for such systems, a compound control method was proposed by Zhang et al. [3]. The generalized notch filter and the repetitive control method are mainly adopted to suppress the harmonic vibration caused by sensor runout and rotor unbalance. That approach indicated the reduction of first- and fifth-order harmonic vibration of the given system by at least 70% and 50%, respectively. Tuned mass dampers (TMDs) are, on the other hand, one of the most robust, basic, and yet efficient passive approaches to suppress harmonic vibrations [4]. For such a case, the additional mass is mounted on the structure needed to protect unwanted vibration. TMDs can be adopted for both rectilinear vibration applications and angular rotational applications. Thus, TMDs have a broad range of applications. For instance, Nerubenko et al. [5] proposed an energy harvesting tuned mass damper in the vehicle driveline. The developed device could reduce the harmonic vibration levels for the driveline shaft and effectively harvest the wasted vibration energy to feed autonomous wireless devices.

The traditional passive TMD with a fixed frequency cannot work effectively in the width range of frequency variations. Therefore, specific control techniques for TMDs were proposed to improve the application’s performance in various cases. Gao et al. [6] proposed a frequency-adjustable tuned mass damper (FATMD) to solve this limitation of the traditional passive TMD for structural vibrations. The numerical results indicated that the proposed FATMD could reduce the pedestrian bridge’s vertical vibration under the excitations of pedestrians, escalators, and earthquakes. Beltran-Carbajal [7] proposed a novel active vibration strategy to extend a passive TMD’s vibration suppression capability. The proposed system includes a feedback controller for reference position trajectory tracking tasks on the vibration absorber and an online asymptotic estimation approach of harmonic excitation forces and its time derivatives of a certain order. Based on the simulation results, the fast and effective estimation of the harmonic perturbation forces is verified.

A new control algorithm for semiactive tuned mass dampers (STMDs) with magnetorheological (MR) dampers was experimentally evaluated by Maslanka [8]. In another study, Nishimura et al. [9] proposed an acceleration feedback control, and the controller performance was optimized and modified. The simulations demonstrated that the presented semiactive control algorithm enables the STMD to achieve similar performance to that of the TMD with five times larger mass.

It is noteworthy that the absorption of random vibrations in civil engineering is a classic application for TMDs. In this sense, various control mechanisms for reducing seismic and wind loads from civil structures have been proposed. STMD was proposed by Chey et al. [10] to mitigate structural response due to seismic loads. The STMD system with a reasonable combination of TMD parameters was found to provide better control than the passive system. Due to additional TMD damping provided at optimal damping values that may be unattainable, the acceleration response reduction of the passive system is slightly greater than that of the STMD system. Aldemir [11] used an MR damper to implement the best control for the TMD when it was subjected to a variety of seismic inputs. For all cases studied, the proposed approach is always better than the equivalent passive TMD. Except for the aforementioned semiactive control strategy for TMDs, various approaches have been investigated and implemented for TMD, such as clipped linear quadratic regulator (LQR) [12, 13], linear quadratic Gaussian control (LQG) [14, 15], variations of ground hook control schemes [16, 17], and on-off phase control algorithms [18, 19].

The control algorithm requires a considerable amount of time and memory for online computation since the deemed semiactive techniques involve the solution of differential equations. Thus, such strategies are less dependable and costly [20]. Furthermore, full state feedback is required, which demands the use of more sensors, increasing device complexity and expense. Therefore, the frequency-based control strategy was suggested in this paper as a simplified and more efficient semiactive control strategy for TMDs. The novel idea is inspired by a TMD system's invariant points property and needs only one accelerometer. The technique aims to reduce repetitive harmonic vibrations on a safe frame.

The paper is organized as follows: the mathematical model and control strategy are explained in Section 2. The experimental configuration is then presented. The experimental findings of the proposed control strategy on an electromagnetic tuned mass damper are presented in Section 3. Finally, the key contributions of the paper were outlined and concluded in Section 4.

2. Materials and Methods

2.1. Mathematical Modeling

To begin, consider the traditional TMD configuration, in which the TMD is placed on a secured structure using a conventional damper and coil spring, as shown in Figure 1.

According to Newton’s second law, the equations of motion of the given 2-DOF with the TMD model are as follows:where M is the protected structure incorporated with a spring stiffness K. The TMD device is depicted as a piece of mass m with a spring stiffness k and a viscous damping c. The system is exposed by a kinetic excitation of . The relative displacement between the TMD and the protected structure is represented by .

In this case, the optimized damping and stiffness coefficients for the best attenuation efficiency can be extracted using the optimization techniques described in [21]. As seen in Figure 2, Kopylov et al. [22] suggested an electromagnetic TMD model in which the damping coefficient can be varied by adjusting the load resistance in the electrical circuit.

The viscous damping force fEMF produces an electromotive force eEMF in the electrical circuit, representing the equivalent of the damping force. Rload and Rcoil are the external load resistance and the TMD inherent coil resistance, respectively, while Lcoil donates the TMD inherent coil inductance. Referring to Figure 2, according to Kirchhoff’s law for electrical circuits, equation (2) is obtained:where is an electromechanical coupling coefficient which also could be written as . is the number of coil turns, while is the average magnetic flux density in the air gap and is the coil length across the magnetic flux. consists of the coil resistance and an external load, respectively, as .

Then, according to Lenz’s law and Ohm’s law, the electrical damping coefficient of the TMD is

The total damping coefficient consists of and , where is the electrical damping coefficient (as given in equation (3)), and the mechanical or heat loss damping is symbolled by . It is worth remembering that the damping in equation (3) holds true even though the inductance effects are negligible. The suggested design can be thought of as an electromechanical system with R circuit (EMR) [23]. A circuit like this adds damping between the TMD and the secured structure physically.

Equation (3) shows that the electrical damping is inversely proportional to the external load resistance while mechanical damping, coil resistance, and coupling coefficient are all constants. Thus, an electrical circuit with an adjustable resistor is needed to achieve semiactively regulation of the damping force for such a device. As seen in Figure 3, Ning et al. [24] suggested an approach based on the metal-oxide semiconductor field-effect transistor (MOSFET).

When the MOSFET is turned on, it supplies the circuit with the lowest load resistance (about 0.3 ohms), resulting in the system’s highest electrical damping coefficient (as given in equation (3)). Otherwise, the system’s electrical damping coefficient is likely to be negative. The ON state is represented by a high-level voltage on the MOSFET's gate, while the OFF condition is represented by a low-level voltage. The controller is used to generate a voltage based on the control technique. Since current may only pass from drain to source via the N-channel MOSFET, the rectifier is used to provide current in the correct direction.

In this article, the suggested technique is used to achieve semiactive control dependent on excitation frequency. The amplitudes of the covered structure and the TMD were used as success criteria to test the efficiency of the proposed control strategy under harmonic excitation. The transition functions between the excitation and the output criteria can be obtained by solving the differential equations in equation (1). The following is the transfer function between excitation and amplitude of the covered structure:

The transfer function between the excitation and the TMD relative amplitude is as follows:

2.2. Control Strategy Explanation
2.2.1. Control Strategy Concept Based on the TMD Theory

This paper proposes a novel semiactive control technique for protected structures subjected solely to harmonic excitations. The concept is based on the TMD system's invariant points property (see Figure 1). The ordinates of its appearance on the frequency response are invariant points that are unaffected by damping. As seen in Figure 4, the frequency curve of the covered system intersects at these points, corresponding to various viscous coefficients of the TMD.

It is worth noting that Den Hartog [25] suggested the classical approach of optimizing the damped TMD based on this property. The optimal solution of a system with a TMD without damping (blue dashed line) is in the frequencies between the invariant points and as seen in Figure 4. The undamped TMD has not been widely used because of the undesirable response in the frequency spectrum outside of the invariant points. Therefore, optimized damping systems have been introduced as systems with a rational response in a specific frequency bandwidth (solid red line). However, the optimized damping systems do not perform much better than the undamped TMD case between invariant points. The semiactive frequency-based control (FBC) technique was formulated in this regard.

The FBC technique attempts to control the damping force of the TMD system depending on the excitation frequency so that the TMD system must be totally undamped during the time of excitation with frequencies located between invariant points. The optimized damping is used for frequencies that are outside of the spectrum of the invariant points. The amplitude-frequency response of the TMD system’s safe configuration is calculated using equation (4). The optimized damping reaction of the covered structure is depicted by the solid red line in Figure 4, while the undamped case of the TMD is represented by the blue dashed line. As seen in Figure 4, the protected structure response between the invariant points and with the corresponding frequencies and is the best for the undamped TMD case, while out of this range, the optimized damping TMD performs better. Then, to obtain the values of the frequencies and , the horizontal coordinates of the invariant points are derived from equation (4) by equating the undamped response with the optimized damping response of the protected structure. Thus, the positive roots of this equation equivalent to the corresponding frequencies of the invariant points in terms of mass ratio and properties of the TMD and protected structure can be obtained as in equation (6). The parameters of the system are listed in Table 1.


EquationDescription

The mass ratio (absorber mass/main mass)
The natural frequency of a TMD
The natural frequency of a protected structure
The frequency ratio (natural frequencies)
The forced frequency ratio

The coordinates for these invariant points are obtained for the case with negligible inductance effects. However, in a case of significant inductance effects, the TMD system will be represented as a Zener model with spring and dashpot linked in series [26, 27]. That model requires a different algorithm for finding the coordinates of the invariant points.

2.2.2. Control Algorithm

According to the FBC technique, processing the signal from the accelerometer connected to the protected structure helps to calculate the excitation frequency of the system. The damping force of the TMD can then be set to be minimal depending on the derived value of the frequency if the frequency is in the range located between the invariant points. Otherwise, as defined in Section 2.1, the damping force is set to maximum by switching the MOSFET transistor. Therefore, the law of the FBC strategy has becomewhere is a measured excitation frequency from the acceleration signal and donates the adjustable damping of the TMD. The program code of the control algorithm and the process of deriving the excitation frequency of the system from the protected structure vertical acceleration data are represented in Algorithm 1.

//Connecting libraries:
 #include <avr/io.h>
 #include <avr/interrupt.h>
 //Pin definition:
 //Acceleration Input:
 const int Acc_1 = A2;
 const int Acc_2 = A1;
 //Control output:
 const int SWITCH1 = 4;
 //Variables:
 float f = 0; //frequency of the system excitation;
 int VA_1; //the first measured acceleration;
 int VA_2; //the second measured acceleration;
 unsigned int timerValue; //timer value; //Start the code:
 void setup() {cli(); //cancell general interupptionspinMode(SWITCH1, OUTPUT);// setting the timer 1:
 TCCR1A = 0;
 TCCR1B = 0;
 TCCR1B |= (1 << CS10);
 TCCR1B |= (0 << CS11);
 TCCR1B |= (1 << CS12); //start up the timer }
 void loop() {VA_1 = analogRead(Acc_1); //reading accelerator sensor data;VA_2 = analogRead(Acc_2); //reading accelerator sensor data;if (VA_1 > 440 && VA_2 ≤ 440){TCCR1B |= (0 << CS10);TCCR1B |= (0 << CS11);TCCR1B |= (0 << CS12); //stop the timertimerValue = (unsigned int)TCNT1L | ((unsigned int)TCNT1H << 8); //reading the timer;f = 1/((float)(timerValue) 0.000064); //deriving the frequency;TCNT1H = 0; //resetting the timer;TCNT1L = 0; TCCR1B |= (1 << CS10);TCCR1B |= (1 << CS12);//set the resolution of the timer with a divider 1024; //FBC control law:if (f ≥ 8.2 && f ≤ 10){digitalWrite(SWITCH1,LOW); //set the maximum damping of the TMD;}else {digitalWrite(SWITCH1,HIGH); //set the minimum damping of the TMD;}}VA_1 = 0;VA_2 = 0; }
2.3. Experimental Setup

The architecture of the electromagnetic TMD suggested by the author in previous work is used in this paper for experimental validation. Figure 5 depicts the construction principles of the back-iron design-based electromagnetic TMD. The TMD was mounted on the protected structure via a connecting flange. As Figure 6(a) shows, the protected structure is a cylindrical piece of steel incorporated with the coil spring.

To derive the system's amplitude-frequency response, two piezoelectric accelerometers (AD100S) were fixed on both the TMD moving part and the protected structure, as shown in Figure 6(a). The schematic layout of the experimental setup including both the TMD and the control circuit is given in Figure 6(b). The AtMega 2560 controller was exploited to process the measurements from accelerometers and then to accomplish the control algorithm. The MOSFET IRF520 was parallelly connected to the TMD coil through a rectifier (GBU808). The general schematic layout of the experimental setup is shown in Figure 7. All the parameters of the 2-DOF TMD fabricated prototype system are listed in Table 2.


ParameterSymbolsValue

Mass of the protected structureM41.5 kg
Mass of the TMDM5.5 kg
Stiffness of the protected structureK172827 N/m
Stiffness of the TMDK18426 N/m
Resistance of the coilRcoil513.5 Ω
Inductance of the coilLcoil1.27 H
Number of windingsN9400
Length of the coilL1475.8 m
Electromechanical coupling coefficientkt182.3 T·m

The exploited excitation equipment consists of a vibration controller VT-9008 and a data acquisition platform. The ETS Solutions company’s vibration excitation machine no. MPA403/M124A was used to generate harmonic excitation with a frequency sweep from 5 to 15 Hz. The results of the established experiment are represented in the next section.

3. Experimental Results

The 2-DOF TMD model is built to demonstrate the performance of the proposed FBC strategy compared with that of the passive TMD system. To estimate the performance of each case reasonably, two indices were introduced. The first one is the peak index which indicates the maximum value of the response for the considered range of frequencies. Secondly, the average value of the response for the considered range of frequencies is represented as follows:where and donate the lower and upper limits of the considered frequencies, respectively.

To validate the proposed passive TMD system in the protected structure test-bench implementation, the passive TMD performance was evaluated for three study cases under harmonic excitation with a frequency range from 5 to 10 Hz, and an amplitude of 25010−6 m: (1) open circuit case without damping; (2) damping de = 32.8 N·s/m corresponding to the external resistive load Rload = 500 Ohm; and (3) short circuit case when the damping coefficient is maximum at de = 64.7 N·s/m. As it may cause damage to the protected structure, the case without TMD was not considered. By differentiating the signal derived from the accelerometers, which are depicted in Figure 7, the protected structure and TMD's amplitude response were obtained, as shown in Figure 8.

It was confirmed that with increasing the damping coefficient of the passive TMD, the amplitude of the protected structure was reduced considerably. As seen in Figure 8, the peak index IP decreased by 71% when considering the two cases with full usable damping (solid green line) and without damping (dashed red line). The device with passive and operated TMD was then subjected to harmonic excitation with a frequency range of 6–14 Hz and an amplitude of 12510−6 m to demonstrate the benefit of using the proposed FBC strategy. Figure 9 shows the related amplitude-frequency responses of the covered structure mass for both the passive and FBC controlled scenarios.

It is seen that such a control policy indicated considerable improvements in the protected structure mitigation performance over the case when the TMD is passive with maximum available damping de = 64.7 N·s/m. Regarding the average value (IA) of the protected structure response, the FBC strategy achieved a reduction of 14% compared to the passive system case. Also, the peak index was reduced by 3%. Although the protected structure with the undamped TMD must indicate an almost zero response between invariant points, in practice, it did not appear due to the continued presence of the mechanical friction between the TMD upper part and the solenoid. Compared to the system response given in Figure 4, the second peaks of the optimized case and the FBC strategy curves appeared lower as expected. This phenomenon can be explained by the presence of the second modal resonance frequency of the proposed TMD construction, which is mostly oscillating in a horizontal direction. It is worth noting that the control was executed with the compromised TMD amplitude. Based on the results shown in Figure 10, the TMD peak response for the FBC concept was increased by 14% compared to the passive TMD stroke length, with corresponding peak indices of Ip = 3.03 and 3.49, respectively. This fact should be considered for the correct estimation of the TMD stroke length for such a control policy.

Pinkaew and Fujino [12] found that the best semiactive approach resulted in a 20% reduction in the protected structure’s displacement. Despite the marginally better efficiency (6% better than FBC), optimum control requires full state feedback measurement, which involves more sensors and increases the system complexity and cost significantly. Meanwhile, the suggested technique could be a cost-efficient and effective way to minimize unnecessary harmonic vibrations.

Finally, the controlled system performance was investigated under random vibration. Based on ISO 8608, the random vibration corresponding to the road irregularities class C was taken as an excitation [28]. The acceleration signal was exploited to estimate the performance of the system. However, the proposed algorithm failed to determine the excitation frequency properly. Consequently, the proposed FBC strategy did not have any advantage over the passive TMD system. The experimental results for the protected structure and TMD are given in Figure 11, where the gravitational acceleration  = 9.81 m/s2.

4. Conclusions

This paper proposed the FBC strategy for electromagnetic TMD applied to the protected structure exposed by harmonic excitation. The effectiveness of the proposed control strategy was validated experimentally under harmonic excitation of 5–15 Hz. The effects of the controlled TMD implementation were compared to the results of the passive TMD results. It was found that FBC policy has a significant effect on the mitigation of protected structures. The protected structure experienced a 14% reduction in average vibration, while the peak response was decreased by 3%. The findings demonstrated the benefit of using the suggested control technique only when there is harmonic excitation. This control policy can be used to prevent unwanted harmonic machine-induced vibrations in systems such as motors, driveshafts, flywheels, and rotors. The proposed control strategy did not show any differences under random vibration compared to the passive TMD. Therefore, as a future work for further research of the controlled TMD, it is recommended to investigate semiactive control strategies oriented on random excitations.

In future work, the proposed control algorithm for a Zener model system with substantial inductance should be developed further. Furthermore, the control scheme can be improved to be used by devices that are subject to stochastic vibration.

Data Availability

The data used to support the findings of this study are available from the corresponding author upon request.

Conflicts of Interest

The authors declared no potential conflicts of interest with respect to the research, authorship, and/or publication of this article.

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Copyright © 2021 Semen Kopylov et al. 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.

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