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Linear Systems and Control
Published in Jitendra R. Raol, Ramakalyan Ayyagari, Control Systems, 2020
Jitendra R. Raol, Ramakalyan Ayyagari
One standard way of designing a lead-lag compensator is to place the product Clead(s)×Clag(s) in cascade with the plant. This is shown in Figure 1.66.
Non-linear parameter optimization of power system stabilizers in interconnected multi-machine power systems
Published in Rodolfo Dufo-López, Jaroslaw Krzywanski, Jai Singh, Emerging Developments in the Power and Energy Industry, 2019
The stabilizer gain block determines the amount of damping introduced by the PSS in terms of gain (Kpss). The wash-out block serves as high pass filter with time constant Tw. The lead-lag compensator block provides the appropriate phase lead characteristics to compensate the phase lag between the exciter input and the generator electric torque with time constants T1 and T2. The structure of PSS used is illustrated in Figure 2.
Frequency-Response Design Methods
Published in Arthur G.O. Mutambara, Design and Analysis of Control Systems, 2017
This compensation is roughly equivalent to combining lead and lag compensators in the same design, and so is sometimes referred to as a lead-lag compensator. Hence, it can provide simultaneous improvement in transient and steady state responses. Although lead-lag compensation approximates PID control, the two approaches involve two completely different strategies.
Adopting Robotic Systems to Enhance Vibration Control of Footbridges
Published in Structural Engineering International, 2018
Kevin Goorts, Sriram Narasimhan
The main advantage of experimental modeling is flexibility in the model form. As such, any stiffness eccentricities or complex damping can be intrinsically accounted for. The input-output data used for estimation are the applied force at the top of the UGV and the measured force at the base of the UGV, respectively, which is consistent with the SDOF transmissibility function. The test setup involves positioning the UGV atop four shear-type load cells and applying a constant amplitude sine-sweep of forces encompassing the spectral bandwidth of potentially controlled structures (i.e. 0 to 5 Hz). A total of six trials were conducted with increasing force magnitudes up to 150 N. Forces greater than 150 N applied to the top of the UGV are amplified beyond 400 N at the base, which causes the UGV to slip.11 Frequency response functions (FRFs) were computed for each trial and are presented in Fig. 3 as a shaded area encapsulating the range of responses under different force magnitudes. The inherent nonlinearity is evident in the magnitude plot, particularly at frequencies greater than 3 Hz. Higher forces increase the level of distortion in the pneumatic tires, which in turn yields a greater amplification effect. Second-order transfer function models were estimated for each trial through curve fitting. The second-order models achieved higher fit percentages than the first- and third-order models but failed to capture the phase properties. By adding a first-order lead-lag compensator with a cutoff frequency ten times greater than the range of interest, the phase performance is improved considerably—and with negligible impact on the magnitude. To minimize the approximation error over the full force range, the estimated model corresponding to an input force of 75 N is considered. The resulting experimental UGV model is given by: