Control system for fluid flow distribution

CROSS-REFERENCE TO RELATED APPLICATIONS
The present application is related to two concurrently filed patent applications (W.E. Cases Ser. No. 550,164, filed Nov. 8, 1983 and Ser. No. 649,462, filed Sept. 11, 1984), which are assigned to the same assignee as the present application, and which are entitled "Steam Optimization and Cogeneration System and Method" and "Linear Programming Energy Management Method and Apparatus for Cogeneration of Steam and Power", respectively, the disclosures of which are incorporated herein by reference.
BACKGROUND OF THE INVENTION
The present invention relates to process control in general, and more particularly, to a decoupling technique implementing energy management and/or optimization in fluid distribution for plant consumption.
Therefore, the invention relates to fluid flow distribution systems in general. More particular, the invention involves the controlled distribution of steam from various pressure lines for energy management and/or for steam-power cogeneration in an industrial plant.
In a steam generating plant, steam of selected quality must be distributed so as to satisfy the demand of an industrial plant and in such a way as to save energy and reduce costs. This is in particular the case where turbogenerators are used to concurrently generated electrical power and deliver steam after expansion through the turbine. Then, energy management in distributing steam from boilers, pressure lines and/or turbine extractions is performed, together with optimization in distributing steam and power from the turbogenerators.
Turbine control optimization in steam-power cogeneration is illustrated in copending patent application Ser. No. 550,164.
As a result of control decisions either under energy management or under the line control optimization, control is effected to change fluid flow on selected lines of distribution. Such control, however, interacts through the process, so that control devices which should not be affected will assume different settings and respond adversely by attenuating the intended flow changes. In order to overcome the effects of this interaction, the present invention provides for anticipating such attenuating effects on the basis of the control decisions and to modify control to the extent of the anticipation, thereby to compensate for the interaction simultaneously when effecting control. This approach has been disclosed as "decoupling" in copending patent application Ser. No. 367,830, filed Apr. 12, 1982, now U.S. Pat. No. 4,500,950, under the title "Industrial Process Control Apparatus and Method". As explained there, non-linear control of a multi-unit industrial combustion process may lead to instability due to the interaction of the various units when one of them is being controlled. Decoupling is implemented with a computer treating the inherent interactions with an algorithm based on a set of data gathered between the different units and processed toward a solution applied to the several units when actually passed into control form. Such decoupling concept has been recognized in the aforementioned application as useful in steam turbine-generator control and in energy management systems where control involves extraction valves, governors and reducing valves of the several units in the system. It was observed, then, that changes made to the control device associated with any one generator, if made on a serial basis, will cause a response from another generator due to natural feedback. It was proposed to decouple the control devices from one another in order to assess the effect that the desired change will also have on the others. Having ascertained the correlative changes induced in the others through the use of a microcomputer, the intended change on the particular control device is implemented simultaneously with such correlative changes on all the other devices. Decoupling, there, was applied to damper positioning as part of automatic control of an exhaust stack of a combustion chamber. Decoupling is required, there, to overcome the non-linearity introduced by natural draft in the relationship between the combustion chamber pressure and stack damper position. Decoupling control in effect adds a corrective change to the output of the position controller of each damper member and generates the correct control signal for damper positioning. Moreover, decoupling was, there, exercised by a DDC system running.
The stability problem is compounded with a cogeneration controller such as described in the aforementioned copending patent application Ser. No. 550,164 in that optimization of a multi-unit turbogenerator plant is, in that particular case, effected with mass flow balancing on each unit and on the overall steam flow system, together with cogeneration of electrical power while supplying with the same source of steam a plant demand in steam and cogenerated electrical power. In such a context, the interaction between make-up reducing valves and extraction steam flows, or between independently controlled extraction valves discharging into a common steam header, will cause, through the governor links, instability to a large degree. Where an optimizing steam flow/power distribution has been determined as stated in the aforementioned pending application, changing the setting of only one turbogenerator unit at a time, in a sequence, requires numerous executions in sequence before a new stable and optimum distribution is reached for all flows and all units.
SUMMARY OF THE INVENTION
The invention relates to a system for the distribution of fluid through a plurality of input fluid lines to satisfy a demand of fluid through a plurality of output lines.
Decoupling means are provided to prevent interaction through the system when control effects selective changes in the flow between the output lines to meet the demand of fluid by an industrial process.
An intended change of flow bearing on one of parallel output lines is used by the decoupling means to simulate how it will cause a resulting change or more through the system in another parallel output line, and control is simultaneously carried out on all output lines so affected, while effecting the intended change of flow, thereby to compensate for such resulting changes.
The invention is applicable to a system in which control means is provided for selectively changing the flow between input lines and for concurrently and selectively changing the flow between output lines in accordance with a predetermined criterion. Control is effected under such criterion while exercising compensating changes in accordance with the decoupling means operation.
The invention is applicable where the criterion is energy management only with respect to turbogenerators but also to any energy converting device operating in parallel, e.g. turbo blowers, gas turbines, chillers, etc. . . In another application, where the system includes turbogenerators for cogeneration of electrical power and steam, the invention combines optimization techniques in distributing steam and power to the lowest cost with the decoupling means when implementing an optimum setting between the various input and output lines.
More specifically, the invention is applicable between pressure reducing valves as well as between turbogenerator units.

BRIEF DESCRIPTION OF THE DRAWINGS
FIG. 1 is a block diagram of a cogeneration process used to generate steam and electrical power to an industrial process;
FIG. 2 is a two-turbogenerator group used in the process of FIG. 1 for the purpose of illustration of the preferred embodiment of the invention;
FIGS. 3A and 3B show the steam power characteristics of the two turbogenerators of FIG. 2, respectively;
FIG. 4 illustrates interaction between the control system and the speed and pressure governors and valve actuators typically installed on one of the turbines of FIG. 2, according to one embodiment of the invention;
FIG. 4A illustrates a gating system for the several programs and functions of a computer system controlling a hydraulic-controlled turbogenerator system like the one shown in FIG. 4;
FIGS. 5A-5F are flow charts illustrating the optimization control mode of operation of the cogeneration system used in a preferred embodiment of the invention;
FIG. 5G is a flow chart combining demand control and turbine control pursuant to FIGS. 4, 4A, 6, 7A, 7B and 8-9;
FIG. 6 shows in block diagram the flow of information in the turbine control program implementing the optimization system of FIGS. 1, 2 and 4;
FIGS 7A, 7B, 7C, and 8-9 are flow charts illustrating pressure control effected under optimization and/or demand control;
FIG. 10 illustrates interaction between pressure reducing valves and extraction valves in a turbogenerator system, according to another embodiment of the invention;
FIGS. 11A, 11B and 11C are characteristic curves of parallel valves operating at a common pressure in the system of FIG. 10; and
FIG. 12 is a block diagram like in FIG. 6 but applicable to the embodiment of FIG. 10.

DESCRIPTION OF THE PREFERRED EMBODIMENT
The invention will be described in the context of the EVOP method of optimization disclosed in aforementioned copending patent application (Ser. No. 550,164).
Referring to FIG. 1, a cogeneration process optimization and control scheme is shown in block diagram to illustrate the preferred application of the invention. Production processes PRP require energy demand ED in the form of power PD and steam SD. Power and steam are derived via lines 13 and 26, respectively, from an electrical power and steam cogeneration process CP. Process CP is supplied with fuel (FU) and air (AI) and also with a complement of power (PP) purchased from the tie-line network TL.
A process model computerized system PMD seeks and locates the optimization conditions for the current energy demands along lines 13 and 26 from the cogeneration process. To this effect, system PMD responds: to signals representing the constraints (established by circuit SCO) assigned to the system (power capacity; maximum steam; pressure limits; boiler capacity; throttle flow and valve setting inlet and outlet flow limits; condenser minimum); to signals representing the process model inputs (derived from circuit PI) characterizing the cogeneration process (CP), and the level of energy demand (prescribed by circuit ED) e.g. the total steam and power demand which is required. The process model optimization system PMD establishes optimal set points defined by circuit OST. A DDC control model CMO, optionally updated in accordance with a self-tuning regulator algorithm REG, responds to the set points derived from the optimal set point circuit OST, to the process inputs derived from circuit PI and to the energy demand from circuit ED. The control model unit CMO controls the operation of the cogeneration process CP by causing a control system output circuit CSO to generate command signals, and also controls a circuit POV providing for process overrides in case of contingencies. Moreover, a steady state model SPM is provided, associated with a process model generation and adaptation controller PMGA implementing the optimization method according to the present invention and reflecting the auto/manual status of the units, taking into account whether a unit is ON or OFF-line, acknowledging changing throttle flow coefficients as pressure and/or temperature changes occur.
Referring to FIG. 2, the cogeneration process proper typically includes: one low pressure boiler BLR #8 (typically of 210,000 lb/hour steam capacity at 550.degree. F. under 220 psig); one high pressure boiler BLR #9 (typically of 210,000 lb/hour steam capacity at 825.degree. F. under 850 psig); and a second high pressure boiler BLR #10 (typically of 210,000 lb/hour steam capacity at 825.degree. F. under 850 psig).
Boiler BLR #8 supplies to the plant complementary steam at 220 psig and 550.degree. F., via pipes 20 and 24, for the process in accordance with plant requirements for such steam. In addition, the steam demand SD for steam at 38 p.s.i. and 350.degree. F. is supplied to the production processes PRP (lines 3, 7 and 25).
Boilers BLR #9 and BLR #10, by respective lines 21, 22, lead to a header 23 supplying three parallel distribution lines 1, 6 and 10. Line 1 supplies steam to a double extraction condensing turbine TG5. The extractions from turbine TG5 are supplied to the production processes PRP. One extraction by line 2 onto junction J1 connects with lines 20 and 24, namely for steam at 220 psig and 550.degree. F. The other extraction by lines 3 and 25 is steam at 38 psig and 350.degree. F. Line 4 from the lower pressure stage LP of turbine TG5 goes to the condenser C1. Line 6 from header 23 supplies steam at 850 psi to a single extraction turbine TG6. The single extraction is by line 7 to junction J2 between lines 3 and 25, altogether, for steam at 38 psig and 350.degree. F. Thus, lines 24 and 25 carry steam at 220 and 38 psi, respectively, to the industrial process PRP, as required by the steam demand SD. An indication of SD is derived on line 36 from steam demand sensors SD1 and SD2 coupled respectively to lines 24 and 25 which feed the process PRP. Line 8 from turbine TG6 goes to the associated condenser C2. Under steam expansion and correlative loss of enthalpy in turbine TG5 at the speed of rotation, a generator EG5 generates power P1, which is carried by line 5 to a junction node J3 with line 12 from the tie-line TL of the electrical network. A power demand control sybsystem is associated with line 12. Similarly, a generator EG6 driven by turbine TG6 generates power P2 which is carried by line 9 to the same junction node J3. From junction J3, an amount of power PD flows via line 13 as demanded by the plant. Wattmeters detect P1 on line 5, P2 on line 9 and P.sub.TL on line 12. A complement of power P.sub.TL, as necessary to meet the demand PD, is derived from the tie-line TL by line 12. The required electrical power PD is fed via line 13 to the industrial process PRP.
Complementary steam at 220 psig and 550.degree. F. from line 20 and boiler BLR #8, at junction J1, is added as necessary to the extracted steam from line 2 on turbine TG5. The 38 psi steam of line 3 from turbine TG5 and the one of line 7 from turbine TG6 add their flow beyond junction J2 onto line 25 to the process.
For steam distribution and for regulation purposes, a first bypass valve VV.sub.1 having pressure reduction capability from 850 to 220 psi is installed on line 10 between line 23 and junction J.sub.1 on line 2, so as to bypass the high pressure stage of turbine TG5. A second bypass valve VV.sub.2 having pressure reduction capability from 220 to 38 psi is installed between junction J.sub.4 of line 2 and junction J.sub.5 of line 25, to bypass turbine TG5 between its two stages H and L. These two valves can help to determine how much steam (steam flow H1 measured by a flow meter FM) is extracted on line 2 (VV.sub.1) and how much steam (steam flow L1 measured by a flow meter FM) is extracted (VV.sub.2) from turbine TG5 on line 3 and from turbine TG6 on line 7. In addition, there are a throttle TH1 on line 1 to turbine TG5 and a throttle TH2 on line 6 to turbine TG6, both controlled by the associated governor, e.g. in accordance with the speed of the turbines, to regulate the respective admissions of steam from header 23. Throttle flows T.sub.1 and T.sub.2 are each measured by a flow meter FM. From an overall consideration of the various supplies of steam shown illustratively in FIG. 2, it is observed that, depending upon plant demand SD.sub.1 of steam at 550.degree. F. and 220 psig on line 24, taking account of the boiler capacity (BLR #8, BLR #9 and BLR #10), of turbine consumption via lines 1 and 6, of the extraction at 220 psig from turbine TG5 and line 2, the pressure reducing valve VV.sub.1 will be controlled accordingly to maintain header pressure above a low limit.
Similarly, if necessary, pressure reducing valve VV.sub.2 is actuated in order to supply complementary steam at 350.degree. F. and 38 psig toward junction J.sub.5 so as to satisfy the low limit of pressure for this 38 psi header. It is the object of the method and apparatus according to the present invention to optimize the extraction of steam at 350.degree. F. and 38 psig on either turbine (EX.sub.1 on line 3 from TG5, and/or EX2 on line 7 from TG6) and the generation of electrical power (P.sub.1 on line 5 from EG5 to TG5 and/or P.sub.2 on line 9 from EG6 of TG6) in regard to the cost per unit of steam consumed and the cost per unit of electrical energy purchased, so as to meet the demand SD+PD.
Accordingly, the cogeneration process involves the following variables:
TABLE I______________________________________SYSTEM VARIABLES______________________________________1. Turbogenerator TG5: Throttle flow (T=T1), on line 1.2. 220 # extraction flow (H=H1), on line 2.3. 38 # extraction flow (L=L1), on line 3.4. condenser flow (C=C1), on line 4.5. power (P=P1), on line 5.6. Turbogenerator TG6: Throttle flow (T=T2), on line 6.7. 38 # extraction flow (L=L2), on line 7.8. condenser flow (C=C2), on line 8.9. power (P=P2), on line 9.10. Pressure reducing valve: 850/220# flow (VV1), on line 10.11. 220/38# flow (VV2), on line 11.12. Purchased power: P.sub.TL, on line 12.______________________________________
In addition, a number of constraints are involved in each particular situation. Thus, there is a maximum flow of steam possible through the throttle (TH1, TH2), a maximum power P1, or P2, obtainable from the corresponding electrical generator (EG5, EG6). The following Table II lists the several linear equations involved in the optimization process together with the constraints to be respected for a particular combination of variables.
TABLE II______________________________________LINE FUNCTION DESCRIPTION______________________________________ #1 Turbine TG5 Maximum throttle flow (for T1, line 1) #2 Maximum flow at intermediate pressure (for L1 + C1, lines 3, 4) #3 Maximum 38 psi extraction flow (for L1, line 3) #4 Maximum power (for P1, line 5) #5 Turbine TG6 Maximum throttle flow (for T2, line 6) #6 Maximum 38 psi extraction flow (for L2, line 7) #7 Maximum Power (for P2, line 9) #8 Turbine TG5 Mass flow balance from transform (1) relationship T1 = H1 + L1 + C1 #9 Turbine TG6 Mass flow balance from transform (2) relationship T2 = L2 + C2#10 Turbine TG5 Throttle flow equation from the (3) characteristic curves of FIG. 3A: T1 = 12,000 + 0.75 .times. H1 + 0.5 .times. L1 + 8 .times. P1#11 Turbine TG6 Throttle flow equation from the (4) characteristic curves of FIG. 3B: T2 = 12,400 + 0.5 .times. L2 + 8.57 .times. P2#12 Header HD2 Mass flow balance to generate net (5) process demand SD1 (line 24) SD1 = H1 + (1.124 .multidot. VV1) - VV2#13 Header HD3 Mass flow balance to generate net (6) process demand SD2 (line 25) SD2 = L1 + L2 + 1.085 VV2#14 Power Bus PD = Power Consumption (line 13) (7) where PD = P1 + P2 + P.sub.TL#15 Turbine TG5 Minimum Power#16 Turbine TG5 Minimum Condenser Flow#17 Turbine TG6 Minimum Power#18 Turbine TG6 Minimum Condenser Flow______________________________________
The equations of Table II can be translated by the following Table III into a matrix.
TABLE III__________________________________________________________________________ VV1 VV2 TG5 TG6 850/ 220/ PT1 220 38 C1 P1 T2 38 C2 P2 275 38 KW1 2 3 4 5 6 7 8 9 10 11 12__________________________________________________________________________1 1 240,0002 1 1 140,0003 1 150,0004 1 9,5005 1 135,0006 -1 130,0007 1 9,5008 1 -1 -1 -1 = 09 1 -1 -1 = 010 1 -.75 -.5 -8 = 12,00011 1 -.5 -7.2 = 12,40012 1 1.124 -1 = 135,70013 1 1 1.085 = 47,12014 1 1 1 = 12,74515 1 4,00016 1 10,00017 1 3,00018 1 10,000COST .00672 .00672 .00672 .0435__________________________________________________________________________
The last line in Table III indicates the costs of steam consumed and of power purchased, while the last column illustratively indicates the magnitudes of the constraints existing in the system.
In Table II mass flow equation (1) line #8 merely expresses that for turbine TG5 the quantity of steam entering (line 1 of FIG. 2) is equal to the sum of the quantities of steam existing (lines 2, 3 and 4 of FIG. 2). Similarly, equation (2) (line 9) is the mass flow equation for turbine TG6, translating the fact that the steam entering by line 6 is totally divided between extraction line 7 and condensing line 8 of FIG. 2.
Equation (3) of Table II is a dynamic equation accounting for the expansion of steam coming from the throttle (TH1) as a steam flow T1 through turbine TG5 performing work and generating power (P1) with an extraction of steam (H1, L1) thereafter. Regarding turbine TG5, referring to FIG. 3A, characteristic curves are shown following a linear equation of the general form: T=a.sub.0 +a.sub.1 H+a.sub.2 L+a.sub.3 P. For zero power (P=P.sub.1 =0) and zero extraction (H=H.sub.1 =0, L=L.sub.1 =0), the value of a.sub.0 may be said to represent the minimum steam admitted through the throttle (TH1) in turbine TG5 in order just to overcome inertia and account for losses. This value is represented by the ordinate of the intersecting point A between line L.sub.0 (zero extraction on FIG. 3A) with the vertical ordinate axis (zero power P). OA=12,000 lbs/hour in the illustration shown by the curves of FIG. 3A for turbine TG5. For a given operative point M1 in the second stage of the turbine, (curves (L) in FIG. 3A) situated on the L1 characteristic, a.sub.2 L1 is the vertical translation from B (zero extraction) to M1 (extraction L1). In the example, L1 is equal to 40,000 lbs/hour. In terms of steam flow, the cogenerated power P1 along the power axis is converted from kilowatts into units of steam flow by the coefficient a.sub.3 =8. For the first stage, the operative point M1 is translated horizontally to the zero extraction point n1 (on H.sub.0) in the (H) family of curves. The gain of curves (H) for turbine TG5 are a.sub.1 =0.75 as stated in line #10 of Table II and in line #10 of the matrix of Table III. The ordinate N1 of point n1 on the 60,00 lbs/hour characteristic defines the throttle flow T1 as 119,000 lbs/hour. Thus, in equation (3), for TG5, a.sub.3 =8; a.sub.2 =0.5 and a.sub.1 =0.75.
Similarly, FIG. 3B illustrates with one family of curves the dynamic transformation in terms of steam (lbs/hour) from throttle flow T2 under expansion, in the single stage of tubine TG6, to generate electrical power (P2) and supply steam by extraction to the industrial process, in accordance with equation (4) of Table II. Thus, in equation (4) the coefficients are a.sub.3 =7.2; a.sub.2 =0.5; and a.sub.1 =0.
From a comparison of equations (1) and (3) it appears that by relying only upon mass flow, the controlling variables (T1, H1, L1, C1 and P1 for turbine TG5, and similarly T2, L2, C2 and P2 for turbine TG6) are interrelated. Therefore, only a few of the parameters need to be modified when seeking optimization in the distribution of steam in and between turbines and of generated power. Having chosen those few parameters, all the others are determined by simple mathematical calculations. Once the optimization technique has been exercised and a preferred distribution of steam and electrical power has been found for each and between both turbines, the system is adjusted as explained hereinafter. Accordingly, the throttles (TH1 and TH2) are given a set point and the values for the extractions (EX1 and EX2) as well as the condenser flow (C1 and C2) are also adjusted. In other words, advantage is taken of the cost improvement indicated by the optimization process to satisfy the present demand (SD and PD) of the industrial process.
Referring again to FIG. 3A, for the purpose of illustration, it is assumed that P1, the cogenerated power from turbine TG5, cannot be less than 4000 or more than 9200 kilowatts. These constraints determine the total throttle flows for the two operating points M1 on the 40,000 lbs/hour line (L1), and M2 on the assumed maximum extraction flow line of 100,000 lbs/hour (L2). The steam characteristics of turbine TG5 are shown to include an intermediary flow family of curves (IF) ranging from zero to 30,000 lbs/hour through which operative point M', by i on the zero line and I on the 20,000 lbs/hour line, rejoins a point n' in the (H) family of curves and a point N' on the 60,000 lb/hour line thereof, namely the operative point for the first stage. Accordingly, a maximum throttle flow value TM is defined by the ordinate of N', illustratively 186,000 lbs/hour, the minimum throttle flow value Tm being 119,000 lbs/hour in relation to operative points M', N.
The curves of FIGS. 3A and 3B are given by the manufacturer. They have been generally used in the past in order to calculate the flow versus generated power relationships for a turbine. Advantage has been taken of this in the present invention, since by using only mass flow equations and the mass flow versus power relationship no recourse is necessary to any entropy or enthalpy determination when performing the optimization function.
Reference will now be made to the constraints expressed in the last column of the matrix of Table III, in the light of the installation of FIG. 2. Line #1 of Table III expresses that throttle flow T1 for turbine TG5 has a maximum constraint of 240,000 lbs/hour. Limitations due to section flow are expressed in line #2 for the 38 psi extraction of line 3 and for the condenser line 4, e.g. EX1 and C1 can have a limited combined flow of 140,000 lbs/hour. Also the condenser extraction C1 cannot be less than 10,000 lbs/hour as stated in line #15. Line #3 states that power P.sub.TL derived from the tie-line cannot exceed 6000 KW, whereas line #4 states that P1, the cogenerated power, is less than 9500 KW and more than 4000 KW (line #14). Similarly, for TG6 the constraints are: T2.ltoreq.135,000 lbs/hour; 3000 KW.ltoreq.P2.ltoreq.9500 KW and C.sub.2, .gtoreq.10,000 lbs/hour. Line #10 and #11 translate the linear equations (3) and (4), respectively, of Table II, where T1.gtoreq.12,000 lbs/hour and T2.gtoreq.12,400 lbs/hour.
Lines #12 and #13 are related to the pressure reducing valves VV.sub.1, VV.sub.2 used for pressure reduction by the psi ratios 850/225 (column 10) and 225/38 (column 11). Referring to FIG. 2, pressure reducing valve VV.sub.1 converts steam at 850 psi on line 10 to saturated steam at 225 psi by the addition of desuperheating water, passing it down to junction J1. Steam at 225 psi collects from VV.sub.1, but also from line 2, e.g. the extraction EX1 from TG5. The total steam from junction J4 goes to junction J1 where it adds up with steam from line 20 directly from boiler BLR #8. At header HD2 the steam consumption by the plant from junction J1 is SD1 on line 24. Pressure reducing valve VV.sub.2 converts steam from J4 at 225 psi on line 11 into saturated steam at 38 psi again by the addition of desuperheating water. Junction J5 collects extraction steam at 38 psi from VV.sub.2 and from junction J2 common to line 3 of TG5 and line 7 of TG6. The steam at 38 psi is collected at junction J5 and fed by header HD3 to the plant by line 25 as a steam demand SD2. SD1 and SD2 represent the total steam demand SD of the plant PRP. Accordingly, line #12 of Table III expresses SD1 in terms of high pressure extraction flow H1, the flow from pressure reducing valve VV.sub.1 and also to pressure reducing valve VV.sub.2, with a net flow of SD1 equal to 135,700 lbs/hour, thus, at junction J1. The relationship is:
SD1=H1+1.124 VV.sub.1 -VV.sub.2 (5)
Similarly, line #13 of Table III states SD2 in terms of the flow from pressure reducing valve VV.sub.2 and of 38 psi steam from both TG5 and TG6 for an output at junction J5 of 47,120 lbs/hour. The relationship is:
SD2=L1+L2+1.085 VV.sub.2 (6)
Referring again to FIG. 2, cogenerated power P1 on line 5 from the EG5 generator coupled to turbine TG5 and cogenerated power P2, on line 9 from the EG6 generator coupled to turbine TG6, are added up with complementary power P.sub.TL derived from the tie-line TL by line 12, to provide on line 13 a total power PD which is supplied by line 13 to the industrial plant. In this regard, line #14 of Table III expresses that the total power consumed (columns 5, 9 and 12) is equal to 12,745 kilowatts.
The last line of the matrix of Table III indicates the cost of steam (T1, T2) expanded through turbines TG5, TG6 and the steam passed to the pressure reducing valve VV.sub.1, thus bypassing turbine TG5. It also indicates the cost of complementary power P.sub.TL purchased from the tie-line TL. These costs are illustratively 0.006727 per unit of steam consumed and 0.0435 per unit of electrical energy purchased.
In this case it is more expensive to cogenerate power P1, or P2, through steam expansion through the turbine, than to purchase it from the tie-line. In another situation it could be the reverse. When evaluating the optimal distribution between steam through turbines TG5 and TG6 and between extraction EX1 (line 2), EX2 (line 7), condenser outputs C1, C2 (lines 4 and 8) and power cogenerated P1, P2 (lines 5 and 9) the conclusion as to what the optimal result is will take into consideration whether power purchased P.sub.TL is more, or less costly, than cogenerated power.
The optimization approach used to illustrate the present invention is as disclosed in the aforementioned copending patent application. It consists in applying the aforementioned EVOP method of optimization within the context of the aforestated mass flow treatment of the process variables in a multi-unit turbogenerator steampower cogeneration process. The EVOP method is, as earlier stated herein, explained in an article by Carpenter & Sweeney in Chemical Engineering of July 5, 1965, pp. 117-126. As explained in the application, off-line treatment by the EVOP method is performed with a model based on mass flow balancing in a multiturbogenerator cogeneration installation. Throttle and extraction flow control is, then, effected in accordance with the off-line results. The invention will be explained hereinafter in the context of a two-turbogenerator system, for the purpose of illustration.
Referring again to FIG. 1, the production processes require at a given moment so much steam and so much electrical power (SD and PD). The system according to the present invention is adjusted to control the cogeneration process CP so that, within a very short time, typically the duration of a microprocessing complete calculation with a specially selected algorithm, the optimal proportions of steam flows, to and from TG5 and TG6, and generated as well as purchased power are calculated which will satisfy quantities of steam on line 26 to SD and on line 13 to PD, at minimum cost.
Referring to FIG. 2, within the cogeneration process the allocation of steam and power in accordance with the microprocessing operations and conclusions thereof affects the flows of steam at 220 psi 550.degree. F. (lines 20, 2, 10 and 24) and at 38 psi 350.degree. F. (lines 3, 7, 11 and 25), namely the steam extractions EX1, EX2, for a given steam supply from boilers BLR #8. It also affects the exhaust to the condensers C1, C2. Moreover, the demanded total steam from boilers BLR #9 and BLR #10 which is determined by the throttle flow on lines 1 and 6, is as called for by the governor (GV1 for TG5, GV2 for TG6), the setting of which is fluctuating and controlled in the same process.
Referring to FIG. 4, for turbine TG5, governor GV1 includes a speed load governor TC1 controlling by line 79 the throttle valve TH1. The turbine control system also includes two pressure governors PGV1, PGV2 responsive to pressure signals respectively derived on lines 76 and 76' from pressure transducers PT. Pressure governor GV1 controls by lines 77 actuators V1, V2 and V3 of the high, intermediate and low pressure sections, respectively. Pressure governor GV2 controls the same by lines 78. It is observed that the gain G between a given governor and a given actuator can be less than unity when the signal is provided for the purpose of internal decoupling. Similarly, turbine TG6 is provided with a speed load governor, or throttle controller TC2 and a pressure governor PGV3 (not shown), within the governor GV2, under respective control setting signals for the speed and for the pressure, respectively. A change of extraction .DELTA.EX1 on line 3 and a change of power .DELTA.P1 from generator EG5 are imparted by the computer system CMP after optimization by imposing a reference setting EX1 through line 73 for PGV2 and a reference setting PS1 through line 72 to TC1 for TG5 in FIG. 4. Similarly, CMP controls TG6 to prescribe a new value of EX2 by a reference setting upon PGV3 (not shown) and/or P2 by a reference setting PS2 to TC2 for TG6. The allocation of steam determines the distribution of generated powers P1, P2 between turbines TG5 and TG6 in accordance with the microprocessing operation. Finally, in the optimization evaluation by the computer system CMP, the optimal complement of power P.sub.TL to be derived on line 12 from the tie-line network is also ascertained, such amount of energy purchased from the network depending, in the optimization process, upon whether it is cheaper, or more expensive, to generate power (P1+P2) locally, or to purchase some power P.sub.TL from the network.
The operation of the optimization system will now be described by reference to the flow charts of FIGS. 5A-5F, to the matrix of equations stated in Table III, and to the EVOP model for optimization with microprocessing techniques represented by Table IV hereinafter.
At the start (FIG. 5A) it is ascertained whether there is power generated or not, namely by turbogenerators TG5, TG6. This is a test whether the turbine circuits are set in motion beyond the minimum power level, or whether they have been shut down. This is ascertained at 100. The initial condition, if there is no power, is established at 101 (COND(I)=0). The system then goes to 103 where the throttle flow of each turbogenerator unit (TG5, TG6) is determined using the throttle flow equation of Table III (equation (3) for TG5, equation (4) for TG6). To this effect, powers P1, P2 are sensed with a wattmeter on lines 5 and 9, respectively. The steam extractions (H1, L1) of lines 2 and 3, respectively, for TG5 and (L2) of line 3 for TG6, are sensed by flowmeters mounted on those lines (FIG. 2). Considering equation (3) for the purpose of illustration, which contains at zero output a minimum throttle flow of 12,000 lbs/hr, the values measured are set into the equation as follows:
T1=0.75H1+0.5L1+8P1+12,000 (3)
thereby to derive the throttle flow value T1. The same is done with equation (4) of Table III to derive the value of throttle flow T2 for the TG6 unit.
T2=0.05L2+7.2.times.P2+12,400 (4)
The system then goes to 104, where the mass flow balance, expressed by equations (1) and (2), leads to the determination of the condenser steam C1 and C2, since:
T1=H1+L1+C1 and T2=L2+C2 (2)
These calculations are also effected in accordance with the flow chart of FIG. 5E, as explained hereinafter.
At this stage all parameters P1, T1, H1, L1, C1, P2, T2, L2 and C2 are known. These will be used in applying the EVOP technique with the model of Table IV for optimization as explained hereinafter.
It is observed, at this time, that the model approach is being based on disturbances exercised on the system under the guidance of a planned succession of tests. It is important here to consider how steam flow distribution and power are brought to converge toward an optimal interrelationship.
Once an optimal relationship has been established (at 185, FIG. 5C), control is effected (via line 186, FIG. 5C) in accordance with the present invention as explained hereinafter. It will be shown how steam flows are effectively and automatically distributed between the two turbogenerator units in order to meet the assigned pressure settings.
Referring to FIG. 2, the industrial process PRP, at a given moment, receives via line 13 electrical power PD=P1+P2+P.sub.TL, where P.sub.TL is the amount purchased from the utility company (tie-line TL). It also receives steam SD=SD1+SD2 from headers HD2, HD3 and lines 24 and 25. The steam consumed may be on line 24, steam at 220 psi resulting from the upper stage (HP on line 2) of TG5, or steam bypassed through pressure reducing valve VV.sub.1 from the 850 psi header HD1 (line 21 from boiler BLR #9 through line 24, junction J1 and line 10. The steam of line 24 may also come directly as a complement from line 20 and boiler BLR #8. On the other hand, the steam of line 25 is steam at 38 psi provided either from the L1 extraction section LP of TG5 (line 3) and the L2 extraction of section LP in TG6 (line 7), or it may result from by-passed steam through pressure reducing valve VV.sub.2 from line 2 and junction J4.
The process demand is the sum of the power demand PD=P.sub.1 +P.sub.2 +P.sub.TL and the steam demand SD=SD1+SD2. A computer is provided with input signals representing PD (line 38), SD (line 37), H1 (line 61), L1 (line 62), L2 (line 63), exhaust C1 from the condenser of TG5 (line 64), exhaust C2 from the condenser of TG6 (line 65), P1 (line 66), P2 (line 67) and P.sub.TL (line 68). As a result of computations explained hereinafter, the control process is conducted with command signals K.DELTA.P1 (line 51), .DELTA.P2 (line 52), .DELTA.H1 (line 53), .DELTA.L1 (line 54), and .DELTA.L2 (line 55), to the turbine, and .DELTA.P.sub.TL (line 56) to the tie-line. These control signals derived, in accordance with the present invention, superimpose on the overall management process control of the industrial plant a refining optimization control or adjustment process control, also effected according to the present invention.
The command signal .DELTA.P1 of line 51 goes to the speed setting input of throttle controller TC1 which, in response to a tachometer TC associated thereto in relation to the turbine TG5 and generator EG5, regulates the throttle TH1 in the steam pipe 1 to the high power stage H of the turbine. As a result, the generated power P1 of EG5 on line 5 is in fact regulated by signal .DELTA.P1, so as to achieve generator speed according to the speed setting. In the same manner, signal .DELTA.P2 of line 52 goes to throttle controller TC2 of turbine TG6 and contributes to adjusting the opening of throttle TH2 of steam pipe 6, thereby to modify P2 on line 9 from generator EG6. The extraction EX1=L1 of turbine TG5 is modified by command signal .DELTA.L1 of line 54, while the extraction EX2=L2 is modified on turbine TG6 by command signal .DELTA.L2 of line 55.
Typically, generators EG5, EG6 are AC synchronous machines, so that a change of speed setting entails a change in power. The governors (GV1, GV2) are part of pressure and speed control loops including the throttle controller (TC1, TC2) and the throttle valve (TH1, TH2).
FIG. 4 schematically shows conventional speed and pressure governors and valve actuators installed, for illustration, on turbine TG5. Actuator V1 controls the pressure of the steam in the high pressure section HP of the turbine by controlling throttle TH1 admitting more or less steam from steam line 1 in response to control line 79 from speed governor TC1. Similarly, actuator V2 controls the intermediate flow into the low pressure section LP of the turbine. Pressure sensed via line 75 and pressure transducer PT at the extraction outlet 2 is used by line 76 to establish through pressure governor PGV1 the desired constant 220 psi steam pressure in extraction line 2. Also similarly, actuator V3 controls the admission of steam from the LP section into the condenser section in response to control line 28 from pressure governor PGV2. Pressure, sensed via line 25' and pressure transducer PT at the low pressure outlet 3, is used by line 76' to establish through pressure governor PGV2 the desired constant 38 psi steam pressure in extraction line 3. In addition, pressure governor PGV2 is modified by a setting change .DELTA.EX1 prescribed on line 73 by the computer system CMP as a result of optimization; whereby actuator V3 establishes a steam flow value L1=EX1 at the extraction line 3 and a condenser exhaust flow C1 from line 4. In the same fashion, tachometer TAC by line 74 establishes a power setting P1 onto the speed load governor TC1 which is itself affected by a setting change imposed from line 72 by the computer system CMP as a result of optimization.
Parallel lines from lines 77, 78 and 79 to the two actuators, other than the one controlled as hereabove stated, differ by the provision of gains G less than unity on each such additional lines, in accordance with generally known turbine control practice.
FIG. 4 has been described illustratively for turbine TG5 of FIG. 2. Pressure governor and speed governor are readily conceived in similar terms for establishing a steam extraction EX2 in response to a change .DELTA.EX2 imparted from the computer system and cogenerated power P2 in response to a change .DELTA.P2 imparted from the computer system in the case of turbine TG6 of FIG. 2. A demand control loop is installed, showed illustratively on FIG. 4, extending from the tie-line of the utility company via the associated wattmeter, line 70, demand controller DC and line 71 to the computer system CMP. The demand controller is according to the teachings of U.S. Pat. No. 3,872,286. There is also a decoupling control loop which operates as explained hereinafter. The hydraulic control, by playing on the extractions (EX1, EX2) in accordance with the pressure set points maintaining a given pressure, determines the amount of condenser exhaust (C1, C2). The hydraulic loop maintains the pressure by adjusting the condenser exhaust, throttle flows and speed. When control is exercised either under demand control changing the electrical load distribution in the plant, or under optimization control, or both, the change in the amount of power (P1, P2) cogenerated and tie-line power P.sub.TL drawn is determined by the change of steam flow distribution between the two units and through the decoupling algorithm indicated hereinafter when adjusting the pressure settings.
For a total steam flow T=T1+T2 in header HD1 to units TG5 and TG6, the total steam flow T is equal to the sum of the extractions and condenser flows T=H1+EX1+EX2+C1+C2. Should one of the extractions be fixed, for instance EX1, the other extraction EX2 is equal to T-EX1-C1-C2. A change of power P2 will be effected by adjusting EX2. If the extractions are fixed, adjustment may take place on C1 and C2, e.g. on the condensers, and if C1 is fixed, adjustment will be only on C2 assuming it lies above its low limit. Thus, considering control action on TG6, increasing C2 will increase P2, whereas decreasing EX2 will cause an increase of the power P2 according to generally known turbine flow principles.
More generally, the hydraulic loop will control and maintain the pressure in accordance with condenser exhaust, throttle steam flow and turbine speed, while the EVOP technique according to the invention will adjust the control settings in accordance with the optimum solution found, establishing the relationship between extractions EX1, EX2, the throttle steam flows (T1, T2), the condenser flows (C1, C2), and leading to cogenerated powers P1, P2 and tie-line power P.sub.TL.
Control is effective with a turbine generator unit on automatic (AUTO). Therefore, it is necessary to ascertain whether one turbine, or the other, or both, are on AUTO before practicing the optimization process.
From a general consideration of FIG. 4 which relates to turbine TG5, and of a governor control system similarly applicable to turbine TG6, it appears that with the turbine set on MANUAL, the operator in the plant will establish the settings for the pressure governor corresponding to a chosen and stable operative mode considering actual demand in steam and/or power. Then, the turbines are set on AUTO, whereby the computer system CMP will calculate an optimum setting and/or a demand control setting which entails changes, on lines, 72, 73 of turbine TG5, for instance. The setting changes required to obtain the calculated optimum, or to meet demand control requirements are effected with contactors moved by small motors rotating in either direction (according to the sign of the error from the present setting) during a lapse of time which represents the magnitude of the change (or error to be nullified) to be performed. Thus, the signals outputted by the computer system CMP which, on lines 72 and 73 of FIG. 4 for instance, represent the optimization results, are converted into time lapses of motor operation with the contactors.
Referring to FIG. 4A, the 60 period AC line is coupled to a counter CNT1 synchronized with the zero-crossings. The output of counter CNT1 establishes a 1/10 of a second time interval (typically) defining the resolution of contact closure under the contact closure control program (see CCOCON in the Appendix). FIG. 4A shows by lines 91 and 92 control of the contactor motor control circuit CMOT having a setting change SC imposed by line 88 for the particular process variable (for instance cogenerated power P1 on line 72 of FIG. 4, or the extraction EX1 required on line 73 thereof for the steam on TG5). Circuit CMOT translates on line 96 the control into motion for the contactor CNCT for the same process variable (via line 98).
Line 91 is inputted into a second counter CNT2, the output of which on line 93 defines a time interval occurring every one second (typically). This time interval is used on line 94 for the demand control period count within demand controller DCO (see the demand control section in the Appendix). Therefore every second the time into the demand control period is updated. As a result, at the end of the demand period (typically 15 minutes) the assigned demand limit will be achieved by the demand controller following a first period (4 minutes as stated in the Appendix) of No Control, followed by a Deadband Control period (5 minutes), and finally with a last period of Adjustable Bias and No Deadband Control (last 5 minutes). Control may be by 97 to have load shedding (LDS) and action in the plant by 98' or by 97' to increase the cogenerated power through circuit COPC to compensate for power reduction (for instance on the tie line, P.sub.TL) and maintain the demand PD. Cogenerated power reduction may be by 90 on TG5 or by 90' on TG6. These actions are causing corresponding setting changes SC for the process variables (P1 or P2).
The time interval of line 93 is triggering a third counter CNT3 which establishes on its output line 95 a third time interval of 20 seconds (typically). This is the recurrence of optimization by the optimization controller OPC and of exercising of the demand control algorithm, namely by line 95' to DCO. Accordingly, via 99 on the output of OPC, steam control is effected (circuit (SCO) to provide on line 89 for TG5 an extraction flow EX1, or on line 89' for TG6 an extraction flow EX2, or via line 99' a change of cogenerated power may be required affecting circuit COPC also translated into .DELTA.P1 for TG5 on line 90, or .DELTA.P2 for TG6 on line 90'.
Considering again the optimization process, control is effected at steps 105, 108, 109 and 112-114 of the flow chart of FIG. 5A. If to the question whether only one governor is on AUTO, at 105, the answer is no, the circuit exits by 106, because when both governors are on Manual (MAN), nothing can be done to optimize. If only one is on Manual (MAN), for instance on turbine TG5 at 108 (it is on turbine TG6 at 112), then the extraction EX1=H1+L1 is set on Manual at 109. The reason is that since TG5 is on Manual, control of the steam distribution has to be exercised on EX2 and/or C2 of the other turbine TG6. It is necessary to fix EX1 at a given flow amount. This is done at 109. If the Manual status is on turbine TG6, the reverse situation is indicated by steps 112 and 113. Step 114 raises the question whether, after stages 108 and 112, either extraction has been set on Manual. If it is Yes, they are both placed on Manual and one is adjusted against the other, manually. After this has been done, the system records the initial index AN=1 which initiates the first step of an accumulated number of optimizing steps carried out with a given set of perturbances effected on the EVOP model during optimization, specifically five steps shown at 130 before proceeding with control.
Referring to FIG. 5B, at 120 the total power P and the total extraction are determined on the basis of the inputs of lines 67, 68, 69 for power and of lines 61, 62, 63 for the extractions into the computer system. Line wattmeters and flowmeters are providing this information. In this regard, it is recalled that (at 103) EX1 and EX2 have been determined and that (at 120) the calculation is the sums P=P1+P2+PTL and EX1+EX2=EX. In the latter regard, when necessary, steam flow derivation by pressure reducing valve VV.sub.2 will be taken into account in keeping with column 10 of the matrix of Table III.
At this point reference must be had to the following base model for EVOP optimization of Table IV.
TABLE IV______________________________________ #1 #1 #2 EXTRAC- CON- CON- TION DENSER DENSER FLOW FLOW FLOWTEST EX1 C1 C2 COST______________________________________BASE BASE.sub.1 BASE.sub.2 BASE.sub.3 --1 BASE.sub.1 - a.sub.1 BASE.sub.2 - a.sub.2 BASE.sub.3 - a.sub.3 COST.sub.12 BASE.sub.1 + a.sub.1 BASE.sub.2 - a.sub.2 BASE.sub.3 - a.sub.3 COST.sub.23 BASE.sub.1 BASE.sub.2 + 2a.sub.2 BASE.sub.3 - a.sub.3 COST.sub.34 BASE.sub.1 BASE.sub.2 BASE.sub.3 + 3a.sub.3 COST.sub.4______________________________________
This table is illustrative only. In the example, it applies to two turbogenerators like shown by FIG. 2 in the preferred embodiment of the invention. The table includes three columns for EX1, C1 and C2, respectively. With regard to EX2, it is observed that if the variables selected for introducing a perturbation are the EX #1 flow, the C #1 condenser flow, and the C #2 condenser flow, e.g., if the EX #1 extraction flow and the total EX extraction flow used by the process as steam are known, the extraction flow EX2 from TG6 is known by difference. On the other hand, if the extraction and condenser flows are known, these are used to calculate the throttle flows T1, T2. Finally, from the known throttle flows and extraction flows, the generated power is calculated.
Tie-line power is the total power PD minus the sum of the cogenerated powers P1 and P2. What is the hourly cost established for each line of the experimental design can then be calculated from the sum of throttle flows multiplied by steam cost, plus tie-line power multiplied by purchased energy cost, and is illustratively stated in the last line of Table III.
In the article entitled "Process Improvement with SIMPLEX Self-Directing Evolutionary Operation" by B. H. Carpenter and H. C. Sweeney in Chemical Engineering of July 5, 1965, is described the EVOP method of optimization. This method is based on a matrix of several process variables disturbed by predetermined increments successively in accordance with a series of tests revealing an improved situation, after which, based on the best results attained, a new set of values for the process variables is in turn disturbed, and this is repeated until the results converge on an optimum. These tests have, in the past, been carried out On-Line by perturbing the process. In contrast, advantage is here taken of the fact that the process variables are, as earlier stated, all equated to steam flow from a common steam generating source, including the electrical power which is converted from a related steam flow amount. Mass flow balancing permits an immediate translation of any change in one of the process variables, or more than one, into a change in cost. Therefore, the evolution on the model so incorporated can immediately be evaluated by simulation, thus, without an actual control action yet occurring. The simulation process is pursued until an established optimum steam and power distribution is arrived at. At this stage it becomes available to be reflected back into the system, e.g., by adjusting control loop set points in real time. Control of the turbogenerators and of the associated pressure reducing valves is performed accordingly. As a result, what would otherwise take too much time to hold the assumed conditions in the matrix unchanged can now be effected on a reliable set of facts with the base model in the matrix, taking advantage of the high speed of operation inherent in a microprocessor, for instance.
Referring to Table IV (which is the matrix of the model illustrated for performing the EVOP method according to the present invention), typically four tests are required for each iteration, namely, rows 1-4 following the "base case" (EX1, C2, C2) which is tested at every step (AN) for which a new set of perturbations a.sub.1, a.sub.2, a.sub.3 are being put to test.
Referring to FIG. 5B of the flow chart, at 120 the total power and total extraction drawn by the industrial process are calculated on the basis of the steam flows provided by flowmeters (FM) and the power measured by wattmeters (WM), and with the assist of the calculations made initially at step 103 of the flow chart (FIG. 5A). As a result, there is so much steam SD and so much power PD to be consumed by the industrial process. The system and method according to the present invention are going to ascertain how the steam should be distributed between the two turbines TG5, TG6, in the example, how much generated power is to be distributed between line 5 (P1) and line 6 (P2) and how much power should be purchased (P.sub.TL) from the utility company (line 12 and tie-line TL). It is recalled that at the start of the first iteration in the major or outer loop at 116 (FIG. 5A) AN=1. Then, at 121 in the array WDEL, the deltas, or perturbations, are chosen to be a.sub.1, a.sub.2, a.sub.3 for columns 1, 2, 3 in the matrix of the model (Table IV). At 122 the matrix is zeroed, by erasing all previous data. At 123 the present values of EX1, C1 and C2 known from steps 103 and 104 are assigned to the first row of the matrix and the chosen perturbances applied. Therefore, column 1, line 1 becomes (EX1-a.sub.1); column 2, line 1 becomes (C1-a.sub.2) and column 3, line 1 becomes (C2-a.sub.3) in the matrix. It is necessary at 124, 125 and 126 to reflect into the model the status of the condensers as ascertained at (108, 109), (112, 113) and (114, 115) in FIG. 5A, when carrying EX1, C1 and C2 into the respective claims thereof. Thus, if at 124 either extraction EX1, EX2 is on Manual, then, for column 1 perturbation a.sub.1 must be zero, or WDEL(1)=0. Likewise at 109, if turbine TG5 has the extraction on Manual, at 125 WDEL(2)=0, e.g., there cannot be any perturbation a.sub.2 introduced in column 2. In the same way, WDEL(3)=0 and a.sub.3 =0 if 113 indicates for TG6 and EX2 is on Manual. This is reflected by step 126. Should all states 124, 125, 126 have a zero status, no control is possible. Then at 128 by 129 the system exits. No optimization is possible.
Otherwise, by 168 the system prepares itself for successive iterations with the inner loop at B in FIG. 5C. It is assumed that initialization with a set of values for a.sub.1, a.sub.2, a.sub.3 at 121 has not been repeated more than five times, as ascertained at 160 (FIG. 5D). If it has, the major, or outer, iteration loop is no longer exercised and the optimal solution at 13 and 185 is considered to have been found. Therefore, by 186 the optimization process is terminated and the system goes to demand control where the demand control requirements are combined with the optimal distribution requirements. Combined control requirements are converted into set points such as applied for TG5 by lines 72, 73 to the speed load governor TC1 and pressure governor PGV2 (FIG. 4), in accordance with the present invention. There may also be a testing of the optimal solution against demand control requirements.
Otherwise, until the number 5 has been reached at 130, the system will proceed with the inner loop iteration process with decreasing values of perturbations a.sub.1, a.sub.2, a.sub.3 for the current delta interval AN, up to ten times as indicated at step 134. Initially, the performance criterion (or cost figure) is zeroed (PERCRT=0). The value of N is made zero at 132, so that the inner loop can be started. At 133 the number of iterations are initiated and counted (N=N+1). At 134 the maximum of 10 iterations is registered. If it has been reached by 143, the inner loop operation is switched out, and the major loop at 160 (FIG. 5D) is given another turn (AN=AN+1). Until that time, the EVOP inner loop is exercised from 135 on (FIG. 5B) by the microprocessor as follows.
At 135 the value for line 1 and column 2, namely A(1,2) is checked against the minimum acceptable for condenser flow C1. In this regard, equation #16 of Table II indicates that C1 should not be less than 10,000 lbs/hour.
It is assumed: there is control possible in the system at 128, e.g. by 168 the minor iteration loop can be energized at B; the performance criterion PERCT has been initialized by putting it to zero at 131, at 132 the first step of the minor iteration loop has been initialized by making N=0. Now, at 133, the additional steps are initiated (N=N+1). Upon each such step, the layout of rows and columns of Table IV is examined and for each row the costs are established (cost 1 through cost 4). The costs so determined are computed to ascertain which line has the highest cost from row 1 to row 4. Having found out one row of highest cost, the average for each variable in the remaining three rows is calculated, doubled, then the value of the variable in the highest cost situation, or worst case, it subtracted therefrom. When this has been established for each column (EX1, C1, C2), this is taken as a "new base case" which is now used for the next iteration step (N+1). As shown by step 134, this procedure is pursued only ten times for the initial given value of delta (a.sub.1, a.sub.2, a.sub.3). If this number is exceeded, by 143 and 165, the system goes to D (FIG. 5D) where delta is made smaller and smaller while operating the process. Thus, for say a.sub.1, the successive values of delta are chosen to be a.sub.1, a.sub.1/2, a.sub.1/3, a.sub.1/4 (see 162 in FIG. 5D).
Before starting the minor loop iteration step, however, adjustments are made with the microprocessor in order to ascertain whether any of the variables under perturbation fall under the constraints. A(1,1), A(1,2) and A(1,3) represent the values of the variable of row 1 and the respective columns 1, 2 and 3, according to step 123. These three constraints are as defined by line #16 for C1 (namely 10,000 lbs/hour) and by line #18 for C2 (namely 10,000 lbs/hour) according to Table III.
If C1=A(1,2)>CONDMIN(1) at 135, the system goes by 107 to C. If not, the constraint is exercised by making A(1,2) equal to the minimum CONDMIN(1) by 137 and 138, thereby accepting a penalty which will be compensated for by controlling the extraction EX1 if it is found possible at 139, to the extent that EX1=A(1,1) is larger than the amount by which C1 has been increased at 138. When C1 is increased, power P1 is increased, whereas when EX1 is decreased, power P1 is increased, and conversely. Therefore, EX1 is diminished by the differential amount "Diff", derived at 137 relative to A(1,2) for C1. Action upon EX1 is only possible, however, to the extent that EX1=A(1,1) cannot be negative. This condition is ascertained at 141. If at 151 A(1,1)<0, at 142, A(1,1) is made equal to zero, and the system goes to 145 by 167, where the constraint on C2=A(1,3) is ascertained (CONDMIN(2)). Should, at 145, the difference between A(1,3) and CONDMIN(2) be positive, control with condenser C2 is possible. Otherwise a penalty is accepted at 147 by making C2=A(1,3)=CONDMIN(2), e.g., 10,000 lbs/hour in this instance.
At this point, from 167, the inner loop proper can be exercised as follows:
At 146 there is a call for a calculation of power (P1, P2) which is effected at E and by line 159 in FIG. 5E, as seen hereinafter. The throttle flows T1, T2 are determined as of now, in accordance with 103, and on account of the values sensed or deducted (EX1, EX2, C1, C2, P1, P2). Now at 148 the matrix of Table IV is loaded into rows 2-4 with the values a.sub.1, a.sub.2, a.sub.3 in accordance with row 1. The resulting flow values are ascertained at 149. From T1, T2, EX1, EX2, C1, C2 the values of P1 and P2 are determined by E in FIG. 5E and steps 170 thereof on. To this effect, the throttle equations are used, at 173 for TG5 and at 175 for TG6, and at 174 more generally. At the same time, it is ascertained whether the governor of TG5 (at 171), or the governor of TG6 (at 172), is on AUTO. If TG5 is on AUTO at 171, the throttle flow T1 is adjusted automatically. If not by 173, TH1 is manually set to the calculated value T1. If TG6 is on AUTO at 172, the throttle flow T2 is adjusted automatically. Otherwise, by 175, TH1 is manually set to the calculated value T2.
On the basis of the information obtained with T1, T2, EX1, EX2, C1, C2, the respective values of P1 and P2 for TG5 and TG6 are calculated at 174. In so doing, it is ascertained, however, whether the constraints of Table III for power of line #4 (P1.ltoreq.9500), line #7 (P2.ltoreq.9500), line #15 (P1.gtoreq.4000) and line #17 (P2.gtoreq.3000) are respected. To this effect at 178 the minima of P1 and P2 are exercised manually (after 176 if the corresponding governor is not on AUTO), so that Power(I)=PMIN(I) if it falls below the minimum. The maxima of P1 and P2 are exercised at 180 and manually POWER(I)=PMAX(I) if the maximum is exceeded. On the basis of such assigned values for P1 and P2, the corresponding throttle values T1 and T2 are calculated at 181 from the throttle equation. This may lead to zero power P1, P2 as will appear at 183, and at zero throttle flow in such case, at 184. The system then goes to G. The system also goes to G if P1, P2 remain between maximum and maximum as ascertained at 177.
Having determined P1 and P2 (FIG. 5E) the microprocessor can determine whether additional power P.sub.TL is needed from tie-line TL in order to satisfy the power demand PD. This is found at 187 (FIG. 5F). P.sub.TL is compared to the minimum power to be purchased at 188. If P.sub.TL is smaller than such minimum at 188, the minimum is accepted as a penalty at 190. Then at step 189 it is ascertained whether the calculated throttle flow (T1, T2) exceeds the maximum flow possible through TH1, TH2. If it is exceeded, the throttle estimate is accepted as a penalty reflecting the excessive demand of steam. Finally, the minor iteration loop initiated at 133 (N=N+1) is terminated by calculating the costs for rows 1-4 at 191, in accordance with step 150 of FIG. 5C. From such cost values in rows 1-4 of the matrix of Table IV the worst case is set aside at 151.
As stated above, at 152, the average of the three other lines is made. The average is doubled and the value of the worst case is subtracted, thereby obtaining at 158 a new base case for the new step N preceding at 133 step N+1. At 153 it is ascertained whether the improvement with the new case is <0.2, indicating a convergence. If it is, the system goes to step AN=AN+1 by 165 for another major iteration step.
If the improvement is large enough (>0.2), the system at 154 updates the performance criterion PERCT at 131, and the minor loop iteration is continued as before (N=N+1) until N>10, at which time, by 143, the system effects another major loop iteration (FIG. 5D).
When the major, or outer loop, is exercised, at 160 the introduced perturbation delta (WDEL(I)) is each time at 162 divided by AN1,2,3,4 for the successive steps thereof. Before taking a new value of delta (a.sub.1, a.sub.1/2, a.sub.1/3, a.sub.1/4, and the source for a.sub.2, a.sub.3) it is checked whether the perturbation C1, or C2, becomes smaller than the minimum. If no decrease is made, WDEL(I)=0, at 103. Upon each new line or experimentation under a fractional increment, the new line 1 in the matrix of Table IV is made equal to the preceding base case minus the new perturbation WDEL(I), at 164. After such step AN=AN+1 at 160, the system goes to the minor loop for further testing (FIG. 5C) with ten possible iteration steps as illustrated at 134.
It is observed that the constraints are handled as penalties (higher costs) if high throttle flow or low tie-line power are encountered in a test set. If condenser flow or power encounter constraints, then values are adjusted and throttle flow recalculated so as to generate the appropriate cost within a constrained but valid data set, i.e., in conformity with the model.
If a device is on Manual, the perturbation delta is forced to zero. Similarly, if an extraction flow reaches a limit, or if a condenser flow reaches a minimum, the associated delta is set at zero. By so doing, it becomes locked and virtually removed from the optimizing procedure.
The invention has been described in the context of steam turbines. It is understood, however, that the EVOP method of controlling the distribution of steam and of power is applicable to the optimization of operation of one or more combination turbines, as well. In such case, the condenser no longer exists. Any consideration of condenser flow is then replaced by consideration of an exhaust of the turbine. It is also observed that the EVOP method described in a situation where the throttle to power relationship can be considered as linear, is applicable even when such relationship is non-linear. This is another advantage of the optimization method according to the present invention, that it is not so limited, as the case would be with conventional linear programming techniques, for instance, and therefore can meet less ideal situations of non-linearity.
Referring again to FIG. 2, there is shown there associated with the computer system used to implement the optimization method according to the present invention, a demand controller TLC to implement demand control according to U.S. Pat. No. 3,872,286 of R. E. Putman issued Mar. 18, 1975. For the purpose of this application, the Putman patent is hereby incorporated by reference. In that patent, the demand controller TLC is responsive on line 56 to commands from the computer system block CMP to derive on line 57 an excess demand .DELTA.P requiring that specific electric loads in the plant be shed, so as to maintain the total electric demand below an assigned limit DL, as explained in the patent. Interruptible loads in the plant represent a definite amount of power consumed under specific switching constraints. The demand control system takes into account priorities established between such loads and the constraints imposed by the loads, when determining whether a load, by line 98, should be switched ON, or shed, in order to maximize production while keeping the consumption under an assigned limit during each billing period. In the context of the present optimization method for cogeneration, the amount of power cogenerated is material to the extent that the power demanded from the tie-line P.sub.TL is within or would exceed the requirements for demand control.
Should demand PD be seen to be excessive from predictions made during a 15-minute period, the power P1 on turbine TG5 would be increased above the previously calculated minimum up to the limit of load. Subsequently the load or turbine TG6 would be increased, should turbine TG5 not be able to sustain the required additional load.
A demand control program is provided, the output of which is superimposed as a subprogram on the minimum condenser flow solution of the optimization program by means of an integrator.
TINPER=TINPER+20.0
DEMPJO=4.0* (ENGPRCH+POWER* (DEMPER-TINPER)/3600)
ERROR=DEMPJO-DEMLIM
N=IFIX (ERROR/ALDINCR)
ADDLOAD=ADDLOAD+FLOAT (N)* ALDINCR
IF (ADDLOAD.LT. 0.0) ADDLOAD=0.0
WHERE:
TINPER=time into period (secs.)
DEMPER=demand period (secs.)
ENGPRCH=calculated amount of energy purchased this period (KWH)
POWER=utility tie-line power (KW) e.g. P.sub.TL
DEMPJO=projected demand at end of 15-minute period (KW)
DEMLIM=present 15-minute period demand limit (KW)
ALDINCR=pseudo load increment (KW)
ADDLOAD=load to be added to turbine with lowest condensing power steaming rate (KW)
Referring to FIG. 5G, when at step 185 of FIG. 5C an optimal solution has been found, the system goes by line 186 to step 200 of FIG. 5G which is part of the demand control program operation. Demand control is effected as explained in the U.S. Patent of R. E. Putman, during successive demand periods of say 15 minutes, to see whether the demand is targeted above or below the demand limit DL, calculate the error, exercise a deadband for no control, introduce a bias and decide to select interruptible loads to be shed according to a priority order and weights. The demand period is initiated by a pulse from the demand wattmeter of the utility company sent every 15 minutes. The demand period is typically divided into three elementary periods. The "first period" is a no-control zone which lasts, typically four minutes. The "second period" is a period in which the demand limit includes a fixed bias, and in which the deadband is exercised. It is a zone of control which lasts typically seven minutes, that is, eleven minutes from the fifteen minutes total. The "third period" is the remaining time in the demand period, during which the bias is adjusted down to zero at the end of the demand period and the upper deadband eliminated.
Demand control is performed when the answer to question 200 is NO. Then, at 203 it is determined whether the time period is less than four minutes ("first period"). If it is NO, the system goes to 204 at which step the time remaining in the demand period is calculated. At 205 the projected error is calculated at the end of the period. At 206 the deadband is exercised if there is a negative error which is smaller than the deadband, that is at 207 the error is made zero. Otherwise by 208 the system goes to 209 where the time into the demand period is found to be less or more than eleven minutes ("second period" or not). In the "second period" the system at 212 exercises the fixed bias by adding it to the error and at 213 the deadband is exercised. After the "second period" has lapsed, at 210 the adjustable bias is varied down to zero, and at 211 the error is added to the bias. From 213 ("second period") or from 211 ("third period") the system goes to 214 where the load change is recognized in accordance with the error.
When demand control is not to be exercised (YES at 200, YES at 203), the system goes to 218 from 186, e.g. in accordance with the requirement to optimize control of the turbogenerator units. If demand control is to be exercised, namely at 214 a load change is required equal to the error of 211 or of 213, either interruptible loads will be shed according to the priority schedule as explained in the Putnam patent, thereby not to exceed the demand limit DL, or the turbogenerator units will be used in order to shift power consumed from the tie-line to the cogeneration group. In the latter instance, the system goes to 215 where it is ascertained whether the load change is less than the maximum allowable change.
Demand control has been described by reference to FIGS. 2 and 5G in the context of successive demand periods of constant duration (15 minutes in this instance). It is understood, however, that such demand periods instead of being successive and adjacent may be overlapping in accordance with the technique of a continuously sliding window, each demand period being slightly shifted from the preceding one and from the following one.
At 216 and 217 an integrator function is introduced based on the assumption that condenser generation can possibly absorb the change. Therefore, at 216 condenser generation is made to include the change and at 217, the amount so ascertained is made superior or equal to zero.
At 218 and 219 the system responds both to a demand control change as ascertained at 214 or to an optimization control change ascertained at 186 via 201. This is the situation expressed at the suming points 307 and 308 of FIG. 8.
At 218 is identified and indexed as LL, the turbine with the lower steam rate, that is, the one forwhich it is cheaper to consume steam in generating power. At 219 is identified and indexed as MM, the other turbine, namely the one for which the steam rate is higher. If the condenser generation is not positive at 220, i.e. no demand control needs to be satisfied, it may be possible to cut back on purchased power if this is the more costing source of electrical energy. It is first determined at 221 what the cost of generated power will be. Then, at 222 this amount is compared to buying the same amount of power from the tie-line. If it is less expensive to cogenerate electrical power, at 223 that amount of power (.DELTA.P1 or .DELTA.P2) is produced in order to reduce the tie-line power P.sub.TL and reach the minimum needed.
At 225 either from 220 if the answer is YES or from 223, the maximum increase on LL is the lowest between the reserve power, the reserve turbogenerator and the desired condensing power change. Having determined the change of power to be derived from the low rate turbine LL, it is known at 226 that the change to be made on the other turbine MM is the difference between the total change and the change on turbine LL. At 227 the power outputs of the optimization program are, then, modified by these power changes. Finally, by 228, which is from step 226 or from step 222, the system goes to the turbine control program, which as explained hereinafter involves the difference array 325 of FIG. 6 and the contact control program 331 thereof.
The differences between actual and desired power generated in the above programs will be converted to a time duration of contact closure and control so implemented. Header pressures need to be monitored in order to avoid adjusting extraction set points outside the operating range. The system is designed to function even with one machine out of service. A clock is included for calculating time into the demand period and the period of this clock is reset automatically by the demand period pulse, as explained in the Putman patent. The following analog inputs are provided: throttle flow (one for each); high pressure extraction flow (one for each); low pressure extraction flow (one for each); condenser flow (one for each); the two turbine powers P1, P2; pressure reducing valve VV.sub.1 ; header pressure (header HD #1) and tie-line power P.sub.TL. The digital inputs are: the tie-line KWH meter pulse input and the demand period pulse input. The digital outputs consist of eight contact points. When implementing control for optimization according to this application Ser. No. 550,164 and concurrently demand control, (the latter according to U.S. Pat. No. 3,872,286 of R. E. Putman) a problem of stability arises in cogeneration systems of the type here described.
Power is generated by passing high pressure steam through turbogenerators to produce both power and process steam, pressure reducing valves are commonly included in the system. One of the pressure reducing valves functions is to satisfy an imbalance between total steam demand, and the steam flow through, and power from, the turbogenerators. For system stability these reducing valves normally possess a drooping characteristic, whereby a change in steam flow can only be produced by a change in process steam header pressure, or pressure control setting. However, because pressure changes affect power when control requires changing steam flow distribution and adjusting the turbine extraction valves, interactions will occur which will delay reaching a new equilibrium.
In order to overcome this, the following technique is used. This technique consists in anticipating steam flow distribution changes upon a given intended valve adjustment, such anticipation being taken into account when adjusting the turbine extraction valves. A program used for such anticipation resolves these interactions for a given set of desired changes to steam flow and power. As earlier stated, the program converts the corresponding changes in turbine governor and extraction valve settings to equivalent contact closure durations which are, then, implemented.
Power generated by the turbogenerators (.DELTA.P1, .DELTA.P2) may be the only variable controlled at times. At other times only steam flow changes are required (.DELTA.EX1, .DELTA.EX2). When both types of changes in the pressure settings such as at line 73 for .DELTA.EX1 and at line 72 for .DELTA.P1 in FIG. 4, and on similar lines for turbine TG6 and .DELTA.EX2, .DELTA.P2, a practical problem arises caused by the interaction between the control actuations through the process. When an optimum steam flow/power distribution has been determined by the EVOP system and is to be implemented, changing the setting of only one device at a time in a sequence requires numerous executions of the sequence before the new distribution is finally achieved for all flows. A method is now disclosed for resolving the inherent interactions between equipment i.e. "decoupling" them, prior to making any changes. The devices are then all adjusted simultaneously by the calculated amounts so that the desired set of net changes to the distribution is achieved in just one or two passes. By incorporating a dead band into the control strategy, the likelihood of this objective being achieved is increased.
An associated advantage of this strategy is that by minimizing the frequency of making changes to equipment settings, the life of the regulating devices is increased and maintenance reduced. The decoupling concept of control has been disclosed in another industrial process context in patent application Ser. No. 367,830, filed Apr. 12, 1982, however, in a different context. In that case, decoupling was between the control loop outputs. The decoupling concept is now implemented as shown in FIG. 6 by block 327 where the control decisions of block 325 in furtherance of optimization (DC) and demand control (DC), are treated mathematically by seeking a solution of simultaneous equations according to the Gauss-Jordan method. As a result, the process variables are simultaneously controlled according to the so modified control decisions. Accordingly, decoupling is achieved, and this is effected by control on the various change settings.
Illustratively, with process variables such as shown in FIGS. 2 and 4, namely the setting change .DELTA.P1 for the power cogenerated by turbine TG5, .DELTA.EX1 for the setting change in the extraction flow fed to the plant from TG5, .DELTA.P2 for TG6 and .DELTA.EX2 for TG6, control is according to the matrix given by Table V herebelow: Referring to the system of FIG. 6, the system of equations involved is represented by the matrix of Table V.
TABLE V______________________________________1 2 3 4 .rarw. Outputs to Governors/.DELTA.P1 .DELTA.EX1 .DELTA.P2 .DELTA.EX2 Inputs from EVOP .dwnarw.______________________________________1 -0.004 .DELTA.P1.sup. 1 -0.01 .DELTA.EX1 1 -0.004 .DELTA.P2.sup. -0.01 1 .DELTA.EX2______________________________________
Table V is a matrix showing the interaction upon a set of changes to be implemented.
Referring to FIG. 6, demand control is performed within block DC in response to power demand P.sub.TL (on line 330) from the turbine and a demand limit DL (on line 331) assigned to the plant, e.g. a limit in KWH not to be exceeded within the demand period, for instance, 15 minutes, provided by the wattmeter of the utility company. As a result, computation is performed within block DC in accordance with the teachings of the aforementioned U.S. Patent of R. E. Putman. The decision taken in block DC may be to change P1 and control turbogenerator TG5 (via line 305) accordingly, or to change P2 and control turbogenerator TG6 (via line 306) accordingly, or both. Assuming such a control, the set point setting for the electrical generation by turbogenerator TG5 or by turbogenerator TG6, or for both, will be modified to a new count. Accordingly, on line 305 for TG5 and on line 306 for TG6, a signal representative of such control will be carried to respective summers 307 and 308. These summers are responsive by respective lines 301 and 302 to the control signals derived from the optimization control circuit OC for a power reference P1 for TG5 (line 301) and/or a power reference P2 for TG6 (line 302). Block OC is responsive to signals indicative of the power demand PD=P1+P2+P.sub.TL and to a signal indicative of the steam demand SD in the plant. According to the explanations heretofore given relative to the optimization technique between steam and electrical power, a new power P1 is prescribed on line 301 to summer 307 and a change in power P2 is prescribed on line 302 to summer 308. Block OC also requires definite changes for optimization of steam flow. These signals appear on lines 303 and 304, respectively. The output signals for power derived from summers 307, 308, on lines 309, 310, for P1, P2 respectively, and those EX1, EX2 for steam on lines 303, 304, are inputted in a target array 311. Similarly, an actual array 320 is responsive to actual power representative signals on 316 for TG5, on 317 for TG6 and to actual steam flow indicative signals on line 318 for PRV1, on line 319 for PRV2. A difference array 325 compares the respective output lines 312-315 to the respective output lines 321-324 to provide on lines 326 the existing increments, or decrements .DELTA.EX1, .DELTA.EX2, .DELTA.P1, .DELTA.P2. Within block 327 are solved simultaneously the equations involved in the array 325, typically using a Gauss-Jordan reduction algorithm. The residual time array 329 responsive by line 328 to the solution block 327, provides on line 330 the control requirement effected at 331 by the control program, namely by establishing corrective set points PS1, PS2 (for loops GV1 for TG5 and GV2 for TG6, respectively in FIG. 2) to distribute powers P1, P2, and PGV2 (as shown in FIG. 4 for TG5), PGV3 (not shown for TG6) to distribute the extraction flows EX1, EX2. In this respect, referring to FIG. 7A, the task is first to calculate the decoupled outputs. To this effect, at 401 the actual load "ACTARR" (see 320 on FIG. 6) is ascertained with the current values of extraction flows (EX1, EX2) and powers (P1, P2) namely:
ACTARR (1)=GP TG5
ACTARR (2)=W38 TG5
ACTARR (3)=GP TG6
ACTARR (4)=W38 TG6
Then, at 403 the target values for the load (see 311 on FIG. 6) are ascertained, summing up the optimal and demand control assignments for the extraction flows (EX1, EX2) and powers (P1, P2). Thus:
TARGARR (1)=Power (1)
TARGARR (2)=W38 EXT (1)
TARGARR (3)=Power (2)
TARGARR (4)=W38 EXT (2).
At 403 the changes (see 325 on FIG. 6) are calculated in the array "DELIN", while at 404 such changes are constrained within assigned limits. At 405 is ascertained whether the controlled variable is on MANUAL, in such case DELIN(I)=0. At 406 the Gauss-Jordan subroutine is called for (see 327 on FIG. 6). At 407, the outputs (see 330 on FIG. 6) of the Gauss subroutine are converted (see 331 on FIG. 6) to equivalent time durations of closure in 1/10 sec increments. At 408 the outputs so derived are constrained within limits.
Referring to FIG. 7B, from 408, the system goes to 410 where the question arises whether the 38 psi header pressure is smaller than the maximum allowable. If it is, by 411 the system goes to 420 of FIG. 7C. If NO at 411, a procedure is initiated to check on the upper limit on the 38 psi header. Accordingly, at 412 the question is raised whether both extractions (EX1, EX2) are on AUTO. It is observed here that when the speed governor is on MANUAL, it is no longer possible for tht turbogenerator to minimize the condenser flow, nor to control the distribution of power with that machine. It remains only to minimize the condenser flow of the other unit. If the answer is NO at 412, two possibilities: at 415 to ask whether EX1 is on AUTO, or at 417 whether EX2 is on AUTO. If it is YES to either one, the step is at 416 (for EX1) to lowr EX1 by -IMAX(2) or at 419 (for EX2) to lower EX2 by -IMAX(4). If the answer is YES at 412, the next step is at 414 to set EX1=-3 and EX2=-2.
In all instances, the system goes to 420 of FIG. 7C. Referring to FIG. 7C, at 420 the question is whether the 38 psi header has a pressure larger than the minimum, and the subsequent step will be to check on the lower limit of the 38 psi header.
At 421, if the answer is NO at 420, the question becomes whether the setting for EX1 is at its maximum, e.g., wide open. If the answer is NO, the system will try to increase the generated power, in order to make more steam available to extraction. Thus at 422, EX1 is increased by maximum. Otherwise, action is on the other machine and at 425 the question becomes whether the setting of EX2 is at its maximum. If the answer is NO, at 426, EX2 is increased by its maximum.
By 424 from 420, or from 422, as well as from 426, the question becomes whether the tie-line power P.sub.TL is larger than the minimum limit assigned. If it is not so, at 427 steps will be taken to lower the generated power, therefore, to raise power P.sub.TL. At 427 the question is whether the power on TG5 (P1) is being decreased. If so, at 429, the question is whether the power on TG6 (P2) is being increased. If NO, at 427, the change on TG5 is reduced by ONE. If YES, at 429, the power change on TG6 is decreased.
Thereafter, at 431, the inputs of the array (303, 304, 310, 311 in FIG. 6) are updated before passing to the output control program (FIGS. 8 and 9).
Referring to the Appendix, there is contained the Gauss-Jordan subroutine. Consider a set of simultaneous equations of the form:
2x.sub.1 -7x.sub.2 +4x.sub.3 =9
x.sub.1 +9x.sub.2 -6x.sub.3 =1
-3x.sub.1 +8x.sub.2 +5x.sub.3 =6
The solution procedure is given step by step by tables B-K and by the algorithm illustrated by the flow chart of FIG. 9.
The Gauss-Jordan method of solving a system of n simultaneously equations in the n unknown is explained in Chapter 5, pages 269-296 of "Applied Numerical Methods" by B. Carnahan, H. A. Luther and J. O. Wilkes published by John Wiley & Sons, 1969. The aforementioned pages of this 1969 publication are hereby incorporated by reference.
The Gauss-Jordan subroutine, found in the Appendix, finds the solution vector corresponding to a set of N simultaneous linear equations using the Gauss-Jordan reduction algorithm with the diagonal pivot strategy. The subroutine begins by first copying the source matrix Q1 into the working matrix Q2. Referring now to matrix Q2, the N by N+1 matrix of coefficients appears in the first N columns of matrix `Q2(N,N1)`, the N1-th column containing the right-hand vector. On the K-th pass of the elimination scheme, K-th row elements are normalized by dividing by the pivot element Q2(K.K). "DETER", the determinant of the coefficient matrix, is updated prior to elimination of all non-zero elements (except for the pivot element) in the K-th column. Should a pivot element be encountered which is smaller in magnitude than "REF", computation is discontinued and "IFLAG" is made equal to unity, so permitting an appropriate comment to be printed by the calling program. Otherwise, "IFLAG" is returned with its value zero.
Starting with the matrix of Table B with the coefficients from the aforestated set of simultaneous equations:
TABLE B______________________________________ 1 2 3 4______________________________________1 2 -7 4 92 1 9 -6 13 -3 8 5 6______________________________________
The procedure consists in dividing the first row by A(1,1) leading to Table C.
TABLE C______________________________________ 1 2 3 4______________________________________1 1 -7/2 2 9/22 1 9 -6 13 -3 8 5 6______________________________________
Then, the first row is subtracted from the second row and the difference is stored in the second row. This is Table D.
TABLE D______________________________________1 2 3 4______________________________________1 1 -7/2 2 9/22 0 25/2 -8 -7/23 -3 8 5 6______________________________________
Table E is obtained by multiplying the new first row by A(1,3) and effectuating a subtraction from the third row.
TABLE E______________________________________ 1 2 3 4______________________________________1 1 -7/2 2 9/22 0 25/2 -8 -7/23 0 -5/2 11 39/2______________________________________
The second row is normalized by dividing by A(2,2), which provides Table F.
TABLE F______________________________________ 1 2 3 4______________________________________1 1 -7/2 2 9/22 0 1 -16/25 -7/253 0 -5/2 11 39/2______________________________________
Thereafter, the new second row is multiplied by A(2,1) and the subtraction made from the first row. The difference is stored in the first row. This is Table G.
TABLE G______________________________________1 2 3 4______________________________________1 1 0 -6/25 88/252 0 1 -16/25 -7/253 0 -5/2 11 39/2______________________________________
The procedure followed thereafter consists in multiplying the new second row by A(2,3) and subtracting from the third row, storing the difference in the third row. This is Table H.
TABLE H______________________________________ 1 2 3 4______________________________________1 1 0 -6/25 88/252 0 1 -16/25 -7/253 0 0 47/5 94/5______________________________________
Table I is obtained by normalizing the third row by dividing by A(3,3).
TABLE I______________________________________ 1 2 3 4______________________________________1 1 0 -6/25 88/252 0 1 -16/25 -7/253 0 0 1 2______________________________________
Table J is formed by multiplying the third row by A(3,1) and subtracting from the first row.
TABLE J______________________________________ 1 2 3 4______________________________________1 1 0 0 42 0 1 -16/25 -7/253 0 0 1 2______________________________________
Next, the third row is multiplied by A(3,2) and subtracted from the second row.
TABLE K______________________________________ 1 2 3 4______________________________________1 1 0 0 42 0 1 0 13 0 0 1 2______________________________________
The subroutine is illustrated by the flow chart of FIG. 9, where N is the number of rows (three, in the numerical example) and the number of columns is at maximum N+1 (four, in the example). At 460 the determinant DETER=1.0 at 461 to initialize the row count K=D. At step 462 the iteration is K=K+1, with at 463 the question whether K exceeds N. If YES at 493 at 494 the flag is set IFLAG=0 and there is a return by 495. If NO at 463, the step at 465 is to have DETER=DETER+A(K,K) effected. Until DETER has been reduced to 1.0E-10, namely at 466, at 468 by 457, KP1=K+1 is effected and J=KP1-1 at 469. The loop at 470 is J=J+1 which is run by 472 and 473 until J>NMAX at 471. At 472 the step defines A(K,J)=A(K,J)/A(K,K). When J>NMAX at 471, the system goes by 474 to 475 where A(K,K)=1, and at 476, I=0 is set in order to initiate the iteration I=I+1 at 477. When I>N at 478 the system returns by 479 to 462 for another iteration K=K+1. When I does not exceed N at 478, the question is raised at 480 whether I=K. If it does, by 481 the iteration is repeated by 481 and 477. If it does not, the question becomes "A(J,K)=0.9" at 483. If it does by 484 and 481 the iteration of step 477 is repeated. Otherwise by 485 the system goes to step 486 where J=KP1-1, then J=J+1 at 487 and until J is no longer larger than N.sub.MAX (at 488) the system returns by 492 and 481 to step 477. If NO at 488, we have at 489:
A(J,J)=A(I,J)-A(I,K).times.A(K,J). Finally, at 490 A(I,K) is made equal to zero, before returning to 477 by 491 and 481.
If at 466, DETER is not larger than 1.0E-10, by 496 the flag is reset (IFLAG=1) and the system returns by 495.
The object here is to set up the desired bit pattern in the register "CCO" and then to make just one I/D call, thus every 1/10 sec. The philosophy of control here is to start all the changes on the contactor settings at the same time. There is no change within the 20 second time period that the system is ascertaining the new changes, thereby to achieve stability and, through decoupling, reaching the desired optimum quickly.
This program is bid regardless every one-tenth second (0.1 sec). If at 442 of FIG. 11 flag COMPLT is false, the program immediately at 442 branches to CALL EXIT so that duty cycle will only be consumed when a contact has to remain closed. Otherwise, by 443, if at 444 on checking NEWDAT, new data is found to be present (NEWDAT=TRUE), by 445 the NEWRESID array is at 446 transferred to the RESIDTM array, after which at 447 NEWDATA is set false at 449, I=I+1. At 450 is determined whether I>N. If not, ICNT is made equal to zero at 451. At 451 ICNT is then forced to zero before Do Loop #1 at 452 is exercised. For each contact in turn, the sign of RESIDTM(I) is first checked, negative by 453 indicating the set point is to be lowered, while positive by 454 indicates that the set point is to be raised.
If lowered, RESIDTM(I) is at 455 incremented (i.e. up towards zero, being negative), CCODN(I) is made true at 456, and at 457 ICNT is incremented.
If raised, RESIDTM(I) is at 458 decremented (i.e. down towards zero, being positive), CCOUP(I) is at 459 made true, and ICNT incremented also at 459.
Should RESIDTM(I) be zero, as seen at 460, the program branches to statement #3 and causes at 461 both CCOUP(I) and CCODN(I) to be made false.
Should ICNT be still zero at 453, at the end of the program, this means that all RESIDTM(I) are not zero and flag CMPLT can now be cleared, permitting CCOCON to branch immediately by 455 to EXIT the new time it is called. CMPLT will be set again if a new adjustment to one of the devices it to be made.
FIG. 4 illustrates extraction control on a turbine provided with an hydraulic governor system. There, electrical control signals representing a desired change for each process variable are derived from the optimization circuit or from the demand controller and applied to the control system so as to change control settings. The control signals are applied to servo-motors actuating contactors after converting into a time mode the magnitude of the intended change. Therefore, the governor system is periodically and discontinuously adjusted in effecting the changes expressed by the computer system for optimization, and/or demand control.
The invention is applicable, however, with another type of turbine control system, in particular where control is in accordance with analog control signals, e.g. signals which continuously fluctuate in magnitude to reflect the desired parameter in absolute value: throttle flow, extraction flow, power in terms of flow. This is the case in practice, where the steam turbine includes a Woodward electric governing extraction control, as generally known.
Decoupling control has been illustrated by reference to FIG. 2 in the narrow context of optimization of the extractions from the turbines alone (TG5, TG6), assuming zero flow in the associated pressure reducing valves, VV2 for instance. Decoupling control admits of a more generalized approach, if this additional parameter is taken into consideration, whereby pressure reducing valve adjustments are added to the EVOP experimental model of Table V. In this case, whenever the plant demand is such that it cannot be satisfied by turbine extractions alone, there will be recourse to pressure reducing valve control to make up the difference.
An illustration of this point is given hereinafter by reference to FIGS. 10, 11A, B, C and FIG. 12.
To reiterate, in cogeneration systems, in which power is generated by passing high pressure steam through turbogenerators to produce both power and process steam, pressure reducing valves are commonly included in the system. One of their functions is to satisfy any imbalances between total steam demand, and the steam flow through and power from the turbogenerators. For system stability these reducing valves normally possess a drooping characteristic, which means that a change in steam flow can only be produced by a change in process steam header pressure. When changing steam flow distribution, this must be anticipated and taken into account before adjusting the turbine extraction valves, the interactions which will otherwise occur delaying the establishment of the new equilibrium.
The program described below resolves these interactions for a given set of desired changes to steam flow and power.
A typical cogeneration system is shown in FIG. 10. For the control of th two turbogenerators, the optimization program of this case will provide not only the recommended extraction flow EX1 from turbogenerator TG1, the recommended power P2 from (and hence steam flow EX2 through) turbogenerator TG2, but also the recommended flow (VV1, VV2) through pressure reducing valves PRV1 and PRV2. These flows will add up to the present total flow through flow control valve FC.
The pressure reducing valves and turbine extraction valve all have essentially linear flow/pressure characteristics, generally as shown in FIG. 11A (for the turbine extraction valve of TG1); FIG. 11B for PRV1) and FIG. 11C (for PRV2). Should they all be controlled independently, a change in set point would need to be made for each device corresponding to the desired change in flow through it, the header pressure P.sub.HDR remaining constant because the total flow will be unchanged. This presents very little of a control problem provided all of the changes are implemented simultaneously.
If however only the turbogenerators are to be controlled, allowing the reducing valves to respond to a change in system pressure (created by the opening of valve FC changing slightly to maintain the same flow at a different header pressure P.sub.HDR) the problem becomes more complex and the interactions present must be resolved before the next magnitude of all changes can be established and then implemented simultaneously. To achieve this the appropriate set of simultaneous equations must be set up in block 327 of FIG. 12 which is analogous to the one of FIG. 6 so as to relate the desired changes in flow .DELTA.VV1, .DELTA.VV2 and power .DELTA.P1, .DELTA.P2 to the physically controlled variables of pressure, or rather changes of pressure by set point SP1 of pressure controller PC1 of valve PRV1, by set point SP2 of pressure controller PC2 of valve PRV2, and by set point SP of the pressure governor PG of the governor GV of TG1 (see FIG. 12). Like in FIG. 6 for the optimization controller OC, the energy management controller EMC of FIG. 12 responds to sensed valves from the industrial process. In this case, besides SD, P.sub.TL, P1 and P2, the inputs are VV1 and VV2, the flows in the pressure reducing valves PRV1, PRV2.
The matrix for the system depicted in FIG. 10 is given by the following Table VI:
TABLE VI______________________________________OUTPUTS.fwdarw. .DELTA.'P1 .DELTA.'P2 .DELTA.'PR1 .DELTA.'PR2 .DELTA.'PX1 .dwnarw.INPUTS______________________________________ 1 .DELTA.P1 1 .DELTA.P2 K2 .DELTA.VV1 K3 .DELTA.VV2 0 -K1 K2 K3 K4 0______________________________________
The variables of Table VI are defines as follows:
.DELTA.P1-Desired change in power on turbogenerator TG1
.DELTA.P2-Desired change in power on turbogenerator TG2
.DELTA.VV1-Desired change in flow through PRV1
.DELTA.VV2-Desired change in flow through PRV2
.DELTA.'PR1-Change in header pressure needed to produce change in flow of .DELTA.VV1
.DELTA.'PR2-Change in header pressure needed to produce change in flow of .DELTA.VV2
.DELTA.'PX1-Change in pressure from TG1 needed by controlling governor GV to produce change in extraction flow EX1.
For reasons of system stability, the two reducing valves PRV1 and PRV2 will almost never be controlling header pressure simultaneously, but it will be arranged to operate over a split range. Thus, either PRV1 is controlling with PRV2 closed; or PRV1 is wide open and PRV2 is then used to control the pressure.
The coefficients in Table VI are as follows:
K.sub.1 -Change in flow on TG2 per unit change in power; (If the turbine characteristic curve is given as EX2=a+b(P2) then K.sub.1 =b=.DELTA.EX2/.DELTA.(P2)
K.sub.2 -Change in flow through valve PRV1 for unit change in discharge pressure, and is negative in sign;
K.sub.3 -Change in flow through valve PRV2 for unit change in discharge pressure and is negative in sign;
K.sub.4 -Change in flow for unit change in extraction valve pressure setting, and is positive in sign.
The flow balance equation is established from the consideration that .DELTA.EX2 is given, as is .DELTA.VV1 or .DELTA.VV2; and TG2 must have its extraction valve pressure setting adjusted to compensate for the sum of the other flow differences. Thus:
K.sub.4 EX1=.DELTA.EX2+.DELTA.VV1+.DELTA.VV2
making .DELTA.EX1 the only dependent variable.
However it is not enough merely to change the SP of PGV1 the extraction valve by the amount .DELTA.P1 since this assumes that the header pressure remaind constant. If this were to happen there would be no change through PRV1, or PRV2, and the desired distribution would not be obtained. To allow for this, the total change in pressure setting may be obtained after first solving the set of simultaneous equation from one of the following:
.DELTA.PX1(TOT)=.DELTA.'PX1+PR1
or
.DELTA.PX1(TOT)=.DELTA.'PX1+PR2.
where PX1 is the pressure counterpart of the extraction flow EX1, where PR1 and PR2 are the pressure counterparts of flows VV1 and VV2, respectively, from the pressure reducing valves PRV1, PRV2.
Referring to FIG. 10, a system is shown wherein steam at 850 psi from a boiler BLR1 is fed by line IL1 into an extraction turbine TG1 having a throttle line THL1, an extraction line XT1, a condenser exhaust G and into a back pressure turbine TG2 having a throttle line TH12 and an extraction line XT2. The extraction flow is at 38 psi, into a back pressure turbine TG2 having a throttle line TH12 and an extraction line and so is extraction flow XT2. TG1 and TG2 are coupled to respective electrical generators EG1, EG2. The supply of steam to turbine TG2 is bypassed by a bypass BPL1 including a pressure-reducing valve PRV1, from 850 psi down to 38 psi. In addition, steam at 850 psi from IL is bypassed via a pressure reducing valve PRV3 to a midpressure line MPL at 220 psi. Again, steam at 220 psi is derived via a bypass line BPL2 including a pressure-reducing valve PRV2 down to 38 psi. All outputs of steam at 38 psi are collected by a common line CL and passed via a header HDC onto the low pressure line LPL. Optimum distribution of steam VV1 from PRV1, VV2 from PRV2, XT1 and TG1 and XT2 from TG2 take into account an imposed criterion, for instance the costs of steam from boiler BLR1, of steam at 38 psi directly through PRV1, indirectly through PRV2, or after expansion through a turbine, TG1 and/or TG2. TG1 is a single extraction condensing turbine, whereas TG2 is a balk pressure turbine. Accordingly, power generated by TG2 is more efficient than power generated by TG1. Therefore, extraction EX2 from TG2 is maximized. Since .DELTA.P2 is determining EX2, control to adjust flow in the common line CL (or pressure header HDR at pressure P.sub.HDR) is expected by playing on .DELTA.P1 and on .DELTA.EX1 through pressure setting point adjustment of the pressure governor PGV of TG1. Accordingly, flow and pressure on the common line CL depends on VV1 (flow through PRV1) on VV2 (flow through PRV2) and the extraction flow EX1 from TG1. Referring to FIGS. 11A, 11B, 11C, the linear flow/pressure characteristics of PGV (FIG. 11A) of PRV1 (FIG. 11B) and of PRV2 (FIG. 11C) are represented with their set points half-way (50% flow) between 0% flow and 100% flow, together with the common pressure P.sub.HDR. Set point SP on FIG. 11A is below actual pressure P.sub.HDR, and control can be effected either by reducing such common pressure, or by adjusting the set point thereby, moving the characteristic line in parallel until its middle point SP meets with the actual pressure P.sub.HDR. Set point SP1 on FIG. 11B is above, and a similar remark can be made. With regard to FIG. 11C, it is observed that the characteristic is not intersecting at all the actual pressure level lines. In actuality there is no flow out of PRV2 in this situation.
In the final analysis, a certain flow EX1 through XT1, and/or EX2 through XT2 will be required or imposed. Similarly, it may be that a certain adjustment of PV1, or of PV2 before header HDC has to be made. Whenever control intervenes on one of those lines, an interaction is likely to ocur which will mask the actual implementation of a change, or of a setting under the intended control.

Number	Name	Date
4027145	McDonald et al.	May 1977
4053746	Braytenbah et al.	Oct 1977
4246491	Waldron et al.	Jan 1981
4258424	Giras et al.	Mar 1981
4270055	Ronnen et al.	May 1981
4500950	Putman	Feb 1985

Control system for fluid flow distribution

Information

Patent Number

Date Filed

Date Issued

Inventors

Original Assignees

Examiners

Agents

CPC

US Classifications

Field of Search

US

International Classifications

Abstract

Description

Claims

US Referenced Citations (6)

Non-Patent Literature Citations (1)