CHAPTER 3 IDENTIFICATION AND CONTROLLER DESIGN FOR...
Transcript of CHAPTER 3 IDENTIFICATION AND CONTROLLER DESIGN FOR...
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CHAPTER 3
IDENTIFICATION AND CONTROLLER DESIGN FOR
UNSTABLE SYSTEM
3.1 INTRODUCTION
In this chapter various methodologies used for system identification
and model based controller design are discussed. System identification
techniques such as classical / modified relay based closed loop analysis and
step response test based identification of lower order models with P/PI
controller are explained in detail. In particular, the relay based identification
procedure and P controller based step response test is discussed for unstable
FOPTD model. Further, model based classical and modified structured PID
controller design procedures for time delayed unstable systems are discussed.
A detailed study with classical PID, I-PD, Two Degree of Freedom (2DOF)
PID, setpoint weighted PID (SWPID), PID controller with prefilter, and
double feedback control loop are presented.
3.2 IDENTIFICATION
In model based controller design procedure, simple models
(FOPTD and SOPTD) are used to characterise the dynamics of a given
process. Based on simple dynamic model obtained, the controller parameters
are then computed using existing methods (Johnson and Moradi 2005).
Identification of lower order transfer function models from
experimental data is essential for model based controller design practice.
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Often, derivation of a rigorous mathematical model is difficult due
to the complex nature of chemical processes (Vivek and Chidambaram 2005).
Hence, system identification procedure is a viable tool to develop
mathematical model of t process. A wide range of analytical techniques exist
for the identification of stable systems. However, for unstable systems, only a
limited progress has been made with analytical approaches such as relay
method and step response test. For a class of unstable systems, closed loop
step test with a P/PI/PID controller provides a satisfactory reduced order
model. This model is employed to design a controller.
3.2.1 Relay Based Methods
Astrom and Hagglund (1984) have proposed the relay based
autotuning procedure and it is widely adopted in industries because of its
simplicity. Process model identification using Auto Tuning Variation (ATV)
is one of the successful methods, which is used to identify the lower order
process models (Luyben 1987).
3.2.1.1 Basic relay
The basic block diagram of closed loop relay test is depicted in
Figure 3.1. The classical relay test generates sustained oscillation of the
controlled variable to obtain vital process information such as ultimate gain
( uk ) and ultimate frequency ( u ).
ah4ku (3.1)
uu P
2 (3.2)
where h is the relay height, a is the amplitude and uP is the period of
oscillations in the process output.
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Figure 3.1 Relay based identification scheme
Luyben (1987) have proposed the relay based closed loop test for
the identification of unstable FOPTD process model from the following
equations;
11
Kk2
u2
u (3.3)
0)(tan u1
u (3.4)
where K is the process gain, is the process time constant, and is the
process delay. In this, it is assumed that the process gain or process delay is
known a priori. Li et al (1991) reported that, the model identified by the
symmetrical closed loop relay test offers an error of 27 to -18% in the value
of uk for stable first order systems.
Consider the open loop unstable FOPTD transfer function which is
given as
se1s
K)s(G (3.5)
In the process control literature, the process parameters for the
above model are considered as K =1 and ranging from 0.1 to 0.8. For the
model with K =1 and = 0.1, Marchetti et al (2001) developed unstable
UnstableSystem
+h
-h
Y (S)R (S)
+ _
e
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FOPTD model with K = 1.001, = 0.101, = 0.87 using Basic Relay (BR)
and K = 1.004, = 0.101, = 0.816 with ATV.
Figure 3.2 Nyquist assessment of process with K=1 and = 0.1
Figure 3.2 depicts the Nyquist comparison of real and identified
process models. The model by BR shows the best fit with the real process
compared to ATV.
For )s(G with K =1 and = 0.4, Marchetti et al (2001)
developed a model with K = 1.001, = 0.426 and = 0.953 using BR based
identification. Further the ATV based identification provided K = 0.928,
= 0.396, = 0.757. With a symmetrical relay test, Vivek and
Chidambaram (2005) obtained K = 0.9841, = 0.4372, = 1.1332. The
relay based system identification proposed by Padhy and Majhi (2006)
offered, K = 1, = 0.3998, = 0.9932. The model attained by Liu and Gao
(2008) using the relay test has, K = 1.0001, = 0.4, = 0.9954.
-1 -0.8 -0.6 -0.4 -0.2 0
-0.4
-0.2
0
Real axis
Real processBR modelATV model
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Figure 3.3 Nyquist assessment of process with K=1 and = 0.4
Figure 3.3 shows a Nyquist comparison of real and identified
models. The model by BR, PM (Padhy and Majhi 2006) and LG (Liu and Gao
2008) shows the best fit with the real process. The model obtained by VC
(Vivek and Chidambaram 2005) is better and the model by ATV method
shows larger deviation than other methods considered.
3.2.1.2 Modified relay
In order to improve the performances such as wide range of
applicability compared to conventional relay method and shorter time
duration to reach sustained oscillations, modified relay feedback methods are
proposed.
Tan et al (2006) discussed a preloaded relay to improve the
estimation of critical points. In this method, a gain parameter 'K is
considered to boost the fundamental frequency in the forced oscillations.
Ramakrishnan and Chidambaram (2003) presented an asymmetrical relay
feedback test to improve the estimation accuracy of SOPTD transfer function
-1 -0.8 -0.6 -0.4 -0.2 0
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
Real axis
Real processBRATVVCPMLG
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model. In this method, the relay amplitude is chosen as h and h , which
improves the estimation of critical point compared to a conventional relay
based procedure. Validation of this proposed method is carried out with a
class of stable process models and improved results are achieved. The work
by Hang et al (2002) summarises the developments of relay tuning methods.
The variation in the classical relay autotuning methods such as biased relay
and parasitic relay are elaborately discussed and examined using a class of
SISO and MIMO process models.
3.2.2 Step Response Test
Closed loop step response is one of the practical methods,
considered to identify the reduced order model of unstable processes. The
major merit of this method is, it does not require an additional component like
relay, and the existing controller (P / PI / PID) can be considered to obtain the
necessary closed loop data for model development. In this scheme, the
controller values are selected by trial and error until the system exhibit an
under damped like response (Padmasree and Chidambaram 2006). The
reduced order unstable model is then derived from the process response
details.
3.2.2.1 P controller based step test
The P controller based identification of unstable system is initially
proposed by Srinivas and Chidambaram (1996). This procedure identifies a
closed loop unstable SOPTD model. From the SOPTD model, open loop
unstable FOPTD model is derived. Figure 3.4 depicts the block diagram of P
controller based step response test.
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Figure 3.4 P controller based step response test
It is assumed that, a real unstable process has an estimated transfer
function representation ranging from FOPTD to TOPTD. The unstable
FOPTD model with K =1 and = 0.1 widely discussed in the literature is
considered (Padmasree and Chidambaram 2006, Chen et al 2008). An
existing closed loop reaction curve method (Padmasree and Chidambaram
2006) is employed to identify the model of the said process. In the proposed
study, three process responses namely are considered; the nearly stable
response with approximately null oscillation (small pK value), response with
under damped like oscillation (modest pK value) and response with more
oscillation (high pK value).
Steps in P controller based system identification procedure:
Step 1 : Consider the closed loop system with pK only,
Step 2 : Excite the system with an unity step signal,
Step 3 : Adjust the value of pK until the closed loop system show an
under damped like response,
Step 4 : Calculate the values of pY , vY , t and Y ,
Step 5 : Find the reduced transfer function model of the system using
Equations 3.6 to 3.13,
Step 6 : Validate the model.
P Controller UnstableSystem
Y(s)R(s)
+ _
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Figure 3.5 Parameters for P controller based system identification
where pY = First peak value, vY = First valley value, t = time difference
between pY and vY , Y = Final steady state value for process output.
The parameters of the process model are identified by considering
the following equations;
)1K)(1(P k2
1 (3.6)
1)(K(1)(K)1K(P k2
kk2 (3.7)
pk KKK (3.8)
22 )Vln(
)Vln( (3.9)
YYYYV
P
V (3.10)
where 1P , 2P , V = variables, = damping ratio, kK = closed loop gain.
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The process model parameters such as K , and can be
evaluated using the following mathematical relations;
Process gain ( K ) =)1Y(K
Y
p (3.11)
Process time constant ( ) =)PPt( 21 (3.12)
Closed loop delay ( ) =P
)Pt(2
2
1 (3.13)
P controller based system identification procedure is attempted for
the above said process model and Figure 3.6 presents the process response for
various pK values. When the pK value is small, the damping ration of the
system is large. The increase in pK decreases the damping ratio, so the
oscillation in the system increases.
Figure 3.6 Closed loop reaction curve for various Kp values
0 1 2 3 4 5 6 70
0.5
1
1.5
2
Time (sec)
Kp =4 Kp =5 Kp =6 Kp =7
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Table 3.1 lists the parameters obtained during the P controller
based identification scheme and the identified unstable FOPTD models for
various values of pK . In order to find the model with best fit with real
process, Nyquist plot comparison is attempted.
Table 3.1 Parameters of P controller based step response scheme
S.
NoKp Yp Yv Y t V P1 P2
Identified
Model
1. 4 1.45 1.32 1.33 0.6 1.12 1.73 2.17
K = 0.9994
= 0.3042
= 0.7205
2. 5 1.57 1.18 1.25 0.4 1.12 1.99 2.28
K = 0.9993
= 0.2221
= 0.5804
3. 6 1.70 0.99 1.20 0.4 0.42 1.91 3.84
K = 0.9994
= 0.3043
= 0.7229
4. 7 2.25 0.51 1.13 0.3 0.94 2.83 3.05
K = 1.0000
= 0.1070
= 0.8357
When pK is small (system with small oscillation), the model
mismatch is larger. From Figure 3.7, it is noted that, the model identified with
pK = 7 provides a best model compared to other pK values.
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Figure 3.7 Nyquist comparisons for various Kp values
Figure 3.8 Nyquist comparison of the existing and identified model
-1 -0.8 -0.6 -0.4 -0.2 0 0.2-0.5
-0.4
-0.3
-0.2
-0.1
0
0.1
0.2
Real axis
Real processKp =4Kp =5Kp =6Kp =7
-1 -0.8 -0.6 -0.4 -0.2 0-0.5
-0.45
-0.4
-0.35
-0.3
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
Real axis
Real processBR modelATV modelStep test with Kp=7
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Figure 3.8 shows the comparison of identified process models. The
model obtained with P controller based step response test is validated with a
relay based model developed by Marchetti et al (2001). The model obtained
with pK = 7 is very close to models by BR and ATV methods.
Consider the unstable FOPTD process model with K =1 and
= 0.4. The P based step response test is executed and FOPTD models are
identified with different pK values. When pK = 2, the identified model
parameters are K = 1.001, = 0.3994, = 1.0015; for pK = 2.25, the
model parameters are K = 1.0001, = 0.4121, = 0.9842 and for pK =
2.5, the process model with parameter K = 0.9992, = 0.4207, = 0.9805
are obtained. In this, the model identified with pK = 2 shows the best fit
with the real process compared to other process models.
For an unstable second order process with one unstable pole as
given in Equation 3.14,
1s5.012s1esG
s5.0 (3.14)
Vivek and Chidambaram (2005) identified unstable FOPTD model
with K = 0.8266, = 0.9951, = 1.8757 using conventional relay, the
identification process with improved relay offers K = 0.7534, = 1.0412,
= 2.1642. With a relay feedback test, Liu and Gao (2008) obtained
K = 1.0001, = 1.0486, = 2.1459. Attempted P controller based step
response test with a pK value of 1.5 provides K = 0.9974, = 0.9931,
= 2.2064.
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Figure 3.9 Nyquist comparison for second order process with various
unstable FOPTD models
Figure 3.9 shows the Nyquist comparison of real and identified
models for the process. The relay and improved relay based model by VC
shows larger deviation with the real process. The relay based model by LG
shows better fit with the real process. The attempted relay test provides a
FOPTD model comparatively superior than LG. The above said second order
process is also considered with =1 (Chen et al 2008).
-1 -0.8 -0.6 -0.4 -0.2 0-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
Real axis
Real processRelay (VC)Improved relay (VC)Relay (LG)Step test (Kp=1.5)
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Table 3.2 Step response parameters and identified FOPTD models for
the second order process with = 1
S.
NoKp Yp Yv Y t V P1 P2
Identified
Model
1. 1.20 8.86 4.64 5.99 9.3 0.47 0.43 1.60
K= 1.0001
= 1.5934
= 2.0483
2. 1.275 7.56 2.80 4.63 7.8 0.62 0.52 1.55
K =1.0006
= 1.667
= 2.0143
3. 1.35 6.81 1.61 3.77 7.0 0.71 0.60 1.61
K = 1.008
= 1.664
= 2.1427
Table 3.2 provides the parameters and unstable FOPTD models for
various values of pK . Figure 3.10 depicts the Nyquist comparison of the real
and identified process model. The model for proportional gain 1.275 and 1.35
are approximately similar, and illustrates good fit with real system compared
to the model with pK = 1.2.
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Figure 3.10 Nyquist comparison for second order process with = 1
From the above results, it is evident that the accuracy of model
parameter depends on controller setting. A heuristic algorithm can avoid this
dependence and with this motivation, a heuristic algorithm is proposed and
the proposed algorithm is also used for controller design.
3.2.2.2 PI / PID controller based step test
For the complex unstable systems, P controller based identification
procedure sometime fails to provide the expected model due to large offset.
Hence, a PI controller based system identification technique is considered for
such systems.
Figure 3.11 PI/PID controller based step response scheme
-1 -0.8 -0.6 -0.4 -0.2 0-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
0.3
0.35
Real axis
Real processKp = 1.2Kp = 1.275Kp = 1.35
PI / PIDController
UnstableSystem
Y(s)R(s)
+ _
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The identification procedure for PI based closed loop reaction
curve method is similar to the P controller method, except the initial
parameters to be adjusted are proportional gain pK and integral gain iK
(Padmasree and Chidambaram 2006).
3.3 CONTROLLER DESIGN
Controller tuning is an essential preliminary procedure in almost all
the industrial process control systems. Despite the significant developments in
advanced process control schemes such as predictive control, internal model
control, sliding mode control, PID controllers are still widely used in
industrial control application because of their structural simplicity, reputation
and easy implementation. The merits of PID controller are as follows: (i)
obtainable in variety of structures such as, academic PID, series PID, parallel
PID and IMC-PID (Vijayan and Panda 2011), (ii) provides optimal and robust
performance, (iii) supports online/offline tuning and retuning based on the
process performance requirement, (iv) advanced arrangement such as 2DOF
and 3DOF are possible. Many researchers proposed PID tuning rules to
control various stable and unstable systems by different schemes to enhance
closed loop performance ( ström and Hägglund 1995, 2006; O'Dwyer
2009). For stable systems, PID controller offers a viable result for both the
reference tracking and disturbance rejection. However, for unstable systems,
it can effectively work either for reference tracking or disturbance rejection.
The proportional and derivative kick in the controller also results in large
overshoot and large settling time.
In process control applications, PID and modified structured PID
are still widely used in industrial control system where reference tracking and
disturbance rejection are a major task.
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3.3.1 PID Controller
Industrial PID controllers usually available as a packaged form and
to perform well with the industrial process problems, the PID controller
requires optimal tuning. Figure 3.12 shows the diagram of a simple closed
loop control system. In this structure, the controller Gc(s) has to provide
closed loop stability, smooth reference tracking, shape the dynamic and the
static qualities of the disturbance response (Johnson and Moradi 2005).
Figure 3.12 General closed loop system framework
In process industries, PID controller is used to improve both the
steady state as well as the transient response of the plant. In Figure 3.11, Gp(s)
represent the process under control and Gc(s) is the controller. The main
objective of this system is to make Y(s) = R(s). In this framework, the
controller continuously adjusts the value of Uc(s) until the error E(s) is zero
irrespective of the disturbance signal D1(s) and/or D2(s).
Closed loop response of the system with setpoint R(s), supply
disturbance D1(s) and load disturbance D2(s) can be expressed as,
)s(D)]s(G[)s(G)s(G1
1)s(R)s(G)s(G1
)s(G)s(G)s(Y 1p
CpCp
Cp
Gc(s)Y(s)R(s)
+ _
D2(s)
+
+Gp(s)
D1(s)
+
+E (s) Uc(s)
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)s(D)s(G)s(G1
12
Cp (3.15)
where, the complementary sensitivity function and sensitivity function of the
above loop is represented in Equations (3.16) and (3.17) respectively.
)s(G)s(G1)s(G)s(G
)s(R)s(Y)s(T
Cp
Cp (3.16)
)s(G)s(G11)s(S
Cp(3.17)
The final steady state response of the system for the set point
tracking and the disturbance rejection is presented below,
AsA
(s)(s)GG1(s)(s)GG
xslim(s)Yslim)(yCp
Cp
tR
tR
(3.18)
0s
L(s)(s)GG1
(s)Gxslim)(y 1
Cp
p
tD1
(3.19)
0s
L(s)(s)GG1
1xslim)(y 2
CptD2
(3.20)
where, A = amplitude of the reference signal and L = disturbance amplitude.
To achieve a satisfactory )(yR , )(y 1D and )(y 2D , it is
necessary to have optimally tuned PID parameters.
In this research work, a non-interacting form of PID controller
structure is considered. For real control applications, the feedback signal is
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the sum of the measured output and measurement noise component. A low
pass filter is used with the derivative term to reduce the effect of measurement
noise. The PID structure is defined below:
1N
sT sT
sT11K(s)G
d
d
ipc (3.21)
where pK / iT = iK , pK * dT = dK , N = filter constant.
Figure 3.13 Parallel form of PID structure
Figure 3.13 shows the PID controller. The output signal from the
controller is ;
T0
f
dipC dt
de(t)1sT
Kdte(t)Ke(t)K(s)U (3.22)
The chief limitation of the classical PID structure is a step change
in the reference input R(s) will cause an immediate spiky change in the
control signal )s(Uc . This abrupt change in the controller output is
Gp(s)Y(s)R(s)
+ _
Kp
Ki / s
Kd s / (Tf s+1)
Uc(s)
Gc(S)
E(s) ++
+
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represented as the proportional and/or derivative kick. These kick effects
rapidly change the command signal to the actuator which controls the entire
operation of the plant. The kick effect can be nullified by using modified PID
structures.
3.3.2 Two Degree of Freedom PID
For unstable systems, the one degree of freedom controller fails to
provide a smooth reference tracking performance due to the occurrence of
proportional and derivative kick (Johnson and Moradi 2005). In order to
improve the overall closed loop performance, it is essential to consider a
2DOF PID structure. A detailed study on various 2DOF structures are clearly
presented by Araki and Taguchi (2003).
Figure 3.14 Feedback structure of 2DOF PID
Figure 3.15 Feed forward structure of 2DOF PID
In this research work, an attempt has been made with the Feedback
(FB) and the Feed Forward (FF) 2DOF PID structures. Figure 3.14 depicts the
FB 2DOF structure with a PD controller in the inner loop and a PID controller
C2(s)
Unstablesystem
Y(s)R(s)
+ _C1(s)
E (s) U(s)
_
+
D(s)
+
+
Unstablesystem
Y(s)R(s)
+ _C3(s)
E (s)
U(s)_
+
D(s)
+
+C4(s)
52
in the outer loop. In this structure, the PID controller responds on error signal
)t(e and the PD controller works on the process output )t(y . Hence, the
controller )s(C2 is free from proportional and derivative kick effect and the
response is very smooth compared to classical PID controller.
The outer and inner loop controller values are presented in
Equation (3.23) and (3.24) respectively.
)s(D)1(s
1)1(K)s(C fdi
p1
)s(DK)1(K)1(K fdip (3.23)
)s(DKK)s(DK)s(C fdpfdp2 (3.24)
where ipi /KK , dpd KK , and are controller weighting
parameters ranging from 0 to 1 and )s(D f is the derivative filter term given
by )sN1/(s f .
Figure 3.15 shows the FF type controller structure with a PD
controller in the feed forward loop and a PID controller in the closed loop.
The PID controller responds on error signal )t(e and the PD controller works
on the reference input )t(r .
The controller values for this structure are presented in Equations
(3.25) and (3.26).
)s(DKKK)s(Ds
11K)s(C fdipfdi
p3 (3.25)
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)s(DKK)s(DK)s(C fdpfdp4 (3.26)
In this structure, the number of parameters to be tuned are pK , iK ,
dK , and . The comparative study by Araki and Taguchi (2003) reports
that, even though there exists a structural difference, the 2DOF FB and FF
controller offers similar reference tracking and disturbance rejection
performances.
3.3.3 Setpoint Weighted PID Controller
Figure 3.16 shows the structure of Setpoint Weighted PID
(SWPID) controller widely considered to offer a smooth reference
performance (Padmasree and Chidambaram 2005; Pillay and Govender
2011). In this the number of controller parameters to be tuned is pK , iK , dK ,
and .
Figure 3.16 Structure of setpoint weighted PID control system
Td D(s)
E(s)
UnstableSystem
R(s)Y(s)
_
_U(s)
Kp
D(s)
1-
1-
_
1/Tis
+
+
+
+
+ +
+
+
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The above SWPID structure can be mathematically represented as
follows;
)s(U)s(U)s(U 21 (3.27)
)s(DT)1(sT
1)1(K)s(U di
p1 (3.28)
)s(DTK)s(U dp2 (3.29)
Recently, Chen et al (2008) have discussed a SWPID controller
design for a class of unstable system. The work reports that, based on the
values of setpoint weighting parameters such as and as represented in
Table 3.3, a simple PID-PD controller provides the classical and modified
PID structures.
Table 3.3 Various setpoint weighted controller structures
Weighting parameters Controller
structure
0 0 PID
0 1 PI-D
1 0 ID-P
1 1 I-PD
0 < <1 1 PI-PD
0 < <1 0 < <1 PID-PD
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When = = 0, the structure offers a PID controller which
works based on the error signal )t(e . At t = 0, the )t(e is
maximum, since the PID structure results in large overshoot
because of proportional and derivative kick.
When = 0 and = 1, it represents a PI-D structure. In this,
PI part responds for )t(e and D works on )t(y . In this
structure proportional kick by the P is maximum and the kick
by D is minimum (since, when t=0, )t(e = max, and )t(y =
0). The reference tracking response of PI-D structure is similar
to PID.
When = 1 and = 0, SWPID forms an ID-P structure,
which is free from proportional kick. The effect of derivative
kick by this structure is considerably small and it can provide
a smooth reference tracking response compared to PID, PI-D.
When = 1 and =1, we can get an I-PD structure, which is
free from proportional and derivative kick and offers a very
smooth reference tracking performance.
When ranges from ‘0 to 1’ and = 1, the PI-PD structure is
constructed. Where the PI part works based on equation 3.28
and PD part works based on equation 3.29. From equation
3.28, the observation is that, the value of proportional gain is
)1(*K p . Since, in PI-PD controller, the effect of
proportional kick is 1 times lesser than the PID controller.
In this the PD part is available in feedback loop and it is free
from proportional and derivative kick effect. Since the
overshoot by PI-PD is lesser than PID and PI-D structures.
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3.3.4 PID Controller with Prefilter
Figure 3.17 depicts the structure of prefilter / setpoint filter based
PID controller discussed by Araki and Taguchi (2003). Jung et al (1999)
reported that, when the filter time constant f is set equal to integral time
constant iT , the controller offers a smooth reference tracking performance.
Figure 3.17 Structure of PID controller with prefilter
Recently, Vijayan and Panda (2011) developed analytical
expression to assign the above controller parameters and validated using a
class of stable and unstable process models.
3.3.5 Double Feedback Control Loop
Figure 3.18 depicts the double feedback controller structure. The
inner loop with a P controller is used to stabilise the unstable system and the
outer loop with PID is used to obtain the required reference tracking and
disturbance rejection responses.
FilterPID
ControllerUnstablesystem
Y(s)R(s)
+_
D(s)
+
+
57
Figure 3.18 Double feedback controller structure
Recently, Vijayan and Panda (2012) proposed detailed analytical
expression for the above said controller and validated the performance using a
class of stable and unstable process models. This structure provides smooth
reference tracking performance for unstable FOPTD and SOPTD process
models
3.4 DISCUSSION
In this chapter various system identification procedures and various
controller structures are presented. The relay based system identification
procedure provides better result for unstable system with < 0.693 (Ali and
Majhi 2006; Yu 1999). The modified relay tuning scheme can be used for
more complex system where basic relay method fails (Hang et al 2002). The P
controller step response test provides better result for unstable systems with
< 0.5 (Padmasree and Chidambaram 2006). In conventional P/PI
controller based step response test, the identified model accuracy greatly
depends on the controller setting. Compared to the P controller based
identification procedure, PI controller based method offers better model
accuracy for the system with > 0.5 (Padmasree and Chidambaram 2006).
The simulation study performed in this chapter demonstrates that, the model
R(s)
_
UnstableSystem
Y(s)
+
e
_P1PID
+
58
accuracy can be improved by choosing appropriate value of Kp during the P
controller based step test.
This chapter also summarizes the classical and modified structured
PID controllers such as parallel form of PID, two degree of freedom PID
(feedback and feed forward structures), setpoint weighted PID, PID controller
with prefilter, and double feedback control loop existing in the literature. The
Setpoint Weighted PID (SWPID) controller has five parameters such as Kp,
Ki, Kd, and . In SWPID, by choosing proper values of and , it is
possible to realize the classical and modified structured PID controllers.