Assessment of the Magnetic Hysteretic Behaviour of MR Dampers through Sensorless Measurements

Magnetorheological (MR) dampers are well-known devices based on smart fluids. *e dampers exhibit nonlinear hysteretic behaviour which affects their performance in control systems. Hence, an effective control scheme must include a hysteresis compensator. *e source of hysteresis in MR dampers is twofold. First, it is due to the compressibility and inertia of the fluid. Second, magnetic hysteresis is the inherent property of ferromagnetic materials that form the control circuit of the valve including MR fluid. While the former was studied extensively over the past years using various phenomenological models, the latter has attracted less attention. In this paper, we analyze the magnetic hysteretic behaviour of three different MR dampers by investigating their current-flux relationships. Two dampers operate in flow mode, whereas the third one is a shear-mode device (brake). *e approach is demonstrated using a sensorless magnetic flux estimation technique. We reveal the response of the dampers when subjected to sinusoidal inputs across a wide range of operating conditions and excitation inputs. Our observations of the flux data showed that the hysteresis is influenced by both amplitude and the frequency of the excitation input. *e procedure allows to analyze the magnetic hysteresis independently of other sources of hysteresis in MR dampers; on this basis, more effective damper models and control algorithms can be developed in the future.


Introduction
MR fluids are representatives of smart fluids.ey are suspensions of microsize noncolloidal and low-coercivity particles in a nonconducting carrier fluid.When subjected to magnetic stimuli of sufficient strength, they develop a yield stress [1].e unique feature in addition to high dynamic range, low hysteresis, low power consumption, temperature stability, and extremely fast response has made the material suitable for use in real-time applications of control systems.
e technology has been commercialized by the automotive industry in semiactive vehicle chassis platforms (dampers) or powertrain mounts in particular [2,3].At the same time, the devices have revealed complex nonlinear characteristics due to the rheology of the fluid itself (shear rate versus shear rate behaviour, yield stress versus magnetic field characteristics) and inherent characteristics of the ferromagnetic materials (nonlinear flux density-field strength magnetisation curves, magnetic saturation) that constitute the magnetic circuit of the device.ese contributors have translated into a nonlinear variation of the damper's force output with respect to the electromagnetic stimuli as well as the mechanical input (relative velocity/displacement).In a typical MR damperbased control system as shown in Figure 1, the information from the plant's onboard diagnostics, for example, vehicle's CAN bus, and sensors is processed through a control algorithm.Based on the data, the resulting current command i cmd is computed and sent to the current driver.At a given time instant, the current command results in the input voltage supply u and the output coil current i c .Given the displacement (velocity) (x (v)), the damper generates the output force F. Apart from meeting real-time requirements, there are several factors that make the process complicated: magnetic hysteresis, mechanical (hydraulic) hysteresis, temperature, friction, nonlinear relationship between current (flux) and yield stress, and so on.
In the case of MR dampers, the source of hysteresis is twofold (mechanical/hydraulic and magnetic).First, the uid itself is compressible.e in uence of compressibility is then manifested, for example, as the hysteresis in forcevelocity plots while stroking the damper.is can be related to the dynamics of a relatively heavy MR uid mass being pushed through a long annular ow path whose resistance varies according to the ux-induced yield stress. e e ect can be observed with or without the magnetic eld applied, and it changes with the mechanical excitation frequency as thoroughly discussed in [4].To summarize, the hydraulic hysteresis depends on the current amplitude applied and the mechanical input frequency.As the mechanical input frequency decreases, that hysteresis is also reduced.e hysteresis of magnetic materials that form the magnetic circuit of MR dampers (valves) is of more complex nature and its merits to be analyzed independently from the other sources.
e phenomenon of magnetic hysteresis is typical of any ferromagnetic material.Although certain fail-safe applications take advantage of high coercivity exhibited by speci c materials (hard magnets), soft magnetic (low coercivity) alloys are used in solenoid cores for low energy loss.Carbonyl iron (common solid-phase material of MR uids) suspensions exhibit virtually no hysteresis [5]; however, the hysteresis of speci c ferromagnetic materials constituting the magnetic circuit of the dampers must be taken into account.Contrary to the mechanical hysteresis, the magnetic one does not disappear when the excitation frequency approaches zero, and it manifests itself, for example, as an additional friction force.
e problem of magnetic hysteresis is also typical in control systems featuring electromagnetic components such as solenoid actuators.e behaviour of such systems has been studied extensively in the past [6], and various hysteretic models have been developed to handle the hysteresis.For example, one popular approach is based on the Preisach model in which the hysteresis is a sum of elementary hysteresis loops [7].Also, Jiles and Atherton provided the popular model of magnetic hysteresis (J-A) [8].Its advantage over the other models is that the model parameters can be related to physical properties of ferromagnetic materials [9].e model is suitable for both isotropic and anisotropic magnetic materials [10] and has been extended to incorporate the temperature dependence [11].e model was modi ed to include the eddy currents impact on the hysteresis [12].In another study [13], a rst-order di erential equation links the eld strength H and the ux density B.
e Coleman-Hodgdon model parameters can be identi ed from physical measurements of the major B − H loops.Both Preisach and Coleman-Hodgdon models can be vectorized.e model of Tellinen [14] is a simple scalar approach for solving hysteresis problems, and it uses the limiting hysteresis loop from physical measurements of ferromagnetic materials.
e signi cance of having a good-quality hysteresis model had been recognized early in control studies of MR dampers, and the reader should refer to [15] for a review of suitable phenomenological models as well as [16,17].However, the majority of these studies neglected the magnetic hysteresis or it was not analyzed separately from other sources.In general, the mechanical hysteresis was considered by examining the relationship between force and velocity/position, whereas the eld-dependent hysteresis was considered by investigating the hysteresis between current and force.ere a few notable exceptions.For example, in [18] as well as [19], the Preisach model was applied to identify the hysteretic behaviour of an MR uid.Next, the Preisach approach was used to develop a model of an MR clutch [20].Also, the Coleman-Hodgdon model was used to analyze the magnetic circuit hysteresis of an MR (rotary) clutch [21].e authors identi ed parameters of the model from physical measurements of various ferromagnetic materials used in the clutch assembly.In another study of an MR clutch, a simple hysteretic model was used [22,23].In the model, the hysteresis is modeled by means of a rst-order ordinary di erential equation linking B and H.
e authors claimed the model fast enough to meet relevant criteria for use in real-time control systems.A nite-element model of an MR clutch incorporating the magnetic hysteresis was developed with the J-A model and including uid dynamics and motion dynamics.Recently, in [24], the transient response of a ow-mode MR damper was examined using the inverse J-A model of magnetic hysteresis.
Brie y, the present study is experimental.It is an attempt to reproduce the magnetic hysteretic behaviour of several MR dampers, namely, ow-mode dampers and a rotary shear-mode damper (brake), respectively, through voltage and current measurements followed by o ine integration to obtain magnetic ux.Aspects of this research should be useful for modeling studies and control system design.
e paper is organized as follows.First, we present the MR dampers and describe their electrical parameters and basic geometry.
en, we proceed to highlight the data acquisition system and the experiment details and discuss  Shock and Vibration the excitation input range.Following the discussion, we provide the readers with details on the flux estimation technique and then present the experimental results.Finally, we draw conclusions.

Dampers
Shortly, three different MR dampers were tested as shown in Figure 2. e first damper was a 2010 Audi Quattro MR vehicle damper (Figure 2(a)).e damper is a flow-mode device.e other two dampers were the RD-8040 smallstroke damper operating in the flow mode and the RD-2028 MR shear-mode brake, respectively.e small-stroke damper is presented in Figure 2(b), whereas the rotary brake is presented in Figure 2(c).In the paper, we refer to the automotive damper as MRD1.MRD2 is the small-stroke Lord Corp. damper and MRD3 is their rotary brake.
MRD1 is a long-stroke damper whose coil resistance is approximately 1 Ω at ambient temperature.e device can be operated up to 5 A continuous current for 30 s. e piston rod diameter is 12.4 mm, and the inner cylinder tube is 46 mm.It is a pressurized monotube shock absorber.
MRD2 is also a monotube gas charged damper.Its current range is from 0 to 1 A continuous current (for 30 s), and the coil resistance including connecting cables is 4.4 Ω.For the remaining details, the reader should refer to the hardware's specification [25].
For comparison, MRD3 is a 5 Nm compact brake [26].e device can be operated up to 1 A continuous current, and its coil resistance is 8.9 Ω.Other details of the dampers, for example, core and coil dimensions, coil turns, and the like, control valve geometries are unknown.
For each damper, we measured their current response to (open loop/uncontrolled) voltage step inputs using the test setup described in the sections below.
e (uncontrolled) MRD1 response is shown in Figure 2(a).e current output of MRD2 is revealed in Figure 2(b) and that of MRD3 in Figure 2(c).Moreover, Table 1 contains the summary of response times for the MRD1 damper.Table 2 reveals the same metrics of the MRD2 damper, whereas Table 3 contains the response time summary of the rotary brake MRD3.By definition, the response time t 63 is the time that takes the current to reach 63% of the steady-state level.Similarly, the times t 90 and t 95 indicate the current metrics to achieve 90% and 95% of the steady-state value in the ON state, respectively.Finally, the response times t 37 and t 10 and t 05 indicate the time needed by the current to drop below 37%, 10%, and 5% of the steady-state value.e metrics vary with the step voltage input level.For example, in the case of the damper MRD1, the time t 90 decreases from the initial 62 ms at 1 A down to 35 ms at 5 A. e MRD2 response times are similar to those of MRD1, whereas inspecting the response time summary of MRD3 shows numbers exceeding 200 ms.
Based on the brief review of the step response data and the measured coil circuit parameters, we expected the dampers to show distinct dynamic behaviour to be demonstrated in the following sections of this study.

Test Inputs and Configuration
In this section, we reveal the test rig configuration and sensor details and excitation inputs and then discuss the experiment.
e data acquisition (DAQ) system is illustrated in Figure 3.As shown in the figure, the measurement circuit incorporated a voltage supply, a power driver, and a PC computer with the InTeCo's RT-DAC 4 PCI AD/DA board [27] also running a MATLAB/Simulink model of the measurement system.e power driver's output current is 7 A max.
e AD/DA board's sampling frequency was 1 kHz during the experiments.e measurement system allowed for the acquisition of the supply voltage u(t), the induced coil voltage u c (t), and the current response i c (t) simultaneously.
All dampers were subjected to similar treatment and measurements.In each case, the experiment was split into two sections.In the first part of the test, we measured the behaviour of the dampers when subjected to sinusoidal voltage waveforms of time-varying amplitude: u(t) � At sin(2πft), where A is the amplitude increase/decrease rate in V/s and f refers to frequency.In the second part of the test, we examined the response of the dampers to constant amplitude sinusoidal inputs of voltage.In this experiment series, we varied the voltage input frequency from 1 Hz to 25 Hz in 1 Hz increments: u(t) � U sin(2πft).
In the case of the damper MRD1, the input voltage u(t) was adjusted in such a way to result in peak current levels from 0 to 5 A in 1 A steps.With the damper MRD2, we varied the supply voltage up to 4.4 V, which resulted in peak current 1 A max.In the case of MRD3, the peak voltage was 8.9 V, again resulting in the maximum current level of 1 A. All dampers were air-cooled in an effort to maintain constant temperature.

Flux Estimation
e experiments required implementing a flux estimation procedure that is based on voltage and current measurements.
e flux ϕ is relatively straightforward to be measured directly.Hall probes or magnetostrictive sensors can measure it in the magnetic structures provided there is access to the location of interest, for example, air gap of sufficient size.Alternatively, sensing coils can be employed for the same task (see [28] and [29] as well as [30] or [31]).In this scenario, since there is no physical access to the control valve(s), the flux is estimated from voltage and current measurements via offline integration as highlighted in Figure 4.
Let us then consider the simplest nonlinear lumped parameters model of one coil MR damper as shown in Figure 5. e model includes the input voltage source u(t), the coil resistance R, and the nonlinear inductance L(i).e model equation is then as follows: where u(t) is the supply voltage and λ(t) � Nϕ is flux linkage, ϕ is the magnetic flux, N is coil wire turns, and u c (t) � dλ/dt is the induced coil voltage.By transforming and integrating (1), we get Shock and Vibration   Shock and Vibration e approach is common in control systems for solenoid actuators as well as motor drives [32].Two major problems associated with this method are the measurement of coil resistance and the implementation of a good quality ux integrator [28].While the coil resistance estimate can be rather easily obtained, the ux integrator is not trivial due to the resulting DC bias and drift due to measurement noise.Also, the unknown initial ux value is a problem that needs to be coped with, too.
To handle this scenario, several sensorless solutions have been proposed in the past for induction motors [33][34][35].e authors proposed modi ed integrators or model-based compensation due to the drift.To reduce the DC o set and low-frequency uctuations that were present in the measured data, we simply employed a high-pass lter as seen in Figure 4.

Results: MRD1.
e results involving the vehicle suspension damper are illustrated in Figures 6-12.Speci cally, Figures 6-7 reveal the data obtained by exciting the damper with the nonstationary amplitude voltage input.Figure 6 shows the measured time history of the coil current and the ux.In Figure 7, the dataset was split into two 5 s sections each in order to highlight the damper's output during current rise and current decay phases, respectively.e gure illustrates the plots of current versus voltage and ux linkage versus current.Next, Figures 8-11 show the damper's output when subjected to (voltage) constant amplitude sinusoidal excitation inputs.As already mentioned, the input voltage amplitude was altered in such a way to result in the maximum amplitude of the coil current equal to 5 A at the initial frequency of 1 Hz.Finally, several steadystate characteristics are presented in Figure 12.
Observations of the plots show that increasing the frequency of the input voltage signal resulted in the current First, the hysteresis loop width grows with the input current applied.Second, the presence of hysteresis results in the variation of the magnetic ux linkage signal when increasing and decreasing the coil current.Shock and Vibration

Results: MRD2.
In Figures 13-19, we illustrate the output performance of the small-stroke damper.Again, we first reveal the nonstationary amplitude test (Figures 13 and  14) results followed by the sinusoidal excitation response data shown in Figures 15-19.In this test scenario, the voltage input was varied to result in the peak current of 1 A at the frequency of f � 1 Hz.e data show similar behaviour to that of MRD1 although it is of different magnitude.For example, the calculated inductance data show larger variation range of the parameter from approximately 40 mH to 90 mH (Figure 19(d)).at contrasts, for example, with the inductance data of the damper MRD1 for which the calculated variation range was from approximately 16 mH to 22 mH as revealed in Figure 12(d).Similarly to MRD1, the flux versus current relationship resembles that of magnetic hysteresis.20-26, we show the test output of the rotary damper.In a manner similar to MRD2, we varied the input voltage to result in the peak current of 1 A. is damper produces the highest flux linkage output of the examined dampers (Λ � 0.3 Wb) (Figure 26(c)).It also exhibits the largest coil resistance and the inductance (reaching 400 mH) as shown in Figure 26(d).As seen in Figure 26, the relationship between current and flux linkage is almost linear for smaller currents up to 0.4-0.5 A. e hysteresis shape as seen, for example, in Figure 22 resembles closely the MRD2's characteristics.

Summary
In this paper, we showed and analyzed the experimental results involving three commercial MR dampers.Two dampers were flow-mode devices, and the third one was a shear-mode brake.
e research objective was to reproduce the magnetic hysteretic behaviour of these dampers by investigating the flux versus current relationship.As demonstrated through the response time data, the              Shock and Vibration performance range of the examined dampers was wide.Internal details of the dampers (core/coil geometry, control gap size) were unknown.erefore, only the extraction of flux linkage data from the measurements was possible.e flux was estimated using a sensorless approach which relies on voltage and current measurements of the control circuit followed by offline integration.e technique can be adapted to online measurements provided a simultaneous coil resistance estimate is determined.Also, at the present stage, the flux estimation approach is rid of a drift compensation mechanism.For the online version, a mutation of the algorithm with drift compensation (closed loop correction) needs to be developed.Shock and Vibration e study concerned the dampers' response to sinusoidal excitations.e hysteretic behaviour which we recorded and analyzed was shown to be a complex function of both the frequency and the input current.e shape of the (averaged) flux linkage versus current curve λ − i resembles that of magnetic hysteresis.e λ − i loop shape and width change with the current applied and the input frequency.Apparently, at low frequencies and high current levels, saturation effects were captured.As the input voltage frequency increased, the coil impedance was upgraded which resulted in lower peak amplitudes of the measured current and flux linkage, respectively.e obtained data also show that the flux linkage in the examined structures is affected by eddy currents which also explains the calculated coil inductance drop with the frequency (and the current).Additionally, the inductance deterioration at low currents may have been caused by measurement noise further augmented by the flux integrator.
e results of this series of experiments may be also applicable to self-powered vibration isolation systems with energy harvesters which feature a direct connection between the harvester and the MR damper [36].Recently, this technique was also applied to squeeze-mode MR dampers [37].
e procedure provides means for separating the magnetic hysteresis from other sources of hysteresis in MR dampers so that the specific effects can be analyzed independently.It provides the information for developing more precise damper models and designing effective control algorithms.For example, the study shows that the nonlinearity due to magnetic hysteresis needs to be analyzed separately from the damper's hysteresis due to MR fluid's compressibility for optimum results.It reveals the dependency of the magnetic circuit's characteristics on the current magnitude and frequency of the excitation.Finally, improving the sensorless technique and extending it to other scenarios will be then explored in future, too.

Figure 1 :
Figure 1: Block diagram of an MR damper-based vibration control system.