CHAPTER 3 INFLUENCE OF STATOR SLOTSHAPE ON THE ENERGY CONSERVATION ASSOCIATED WITH THE SUBMERSIBLE INDUCTION MOTORS


 Phoebe Willis
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1 38 CHAPTER 3 INFLUENCE OF STATOR SLOTSHAPE ON THE ENERGY CONSERVATION ASSOCIATED WITH THE SUBMERSIBLE INDUCTION MOTORS 3.1 INTRODUCTION The electric submersiblepump unit consists of a pump, powered by a mediumvoltage threephase induction motor. The power transmission system is integrated with riserpipes. Pipe stacks are flanged together, and consist of riserpipe with the power transmission system, concentrically mounted inside of each section. The power transmission system comprises a protective pipe with the copper conductors mounted inside. The motor is filled with water, and is being continuously circulated inside. The motor unit has forcedwater lubrication. The water is fed down to thrust bearings and the mechanical seal through slots in the stator and returns to the surface through the rotorgap/statorgap and transmission system. 3.2 ANALYSIS APPROACH This chapter presents the performance improvement of submersiblepump sets ranging from 3HP to 7HP, by increasing the efficiency of squirrelcage induction motor. For a threephase induction motor, the stator winding consists of p poles and are distributed in space. The stator winding is usually connected to a threephase balanced voltage source. The resulting currents in the stator produce a rotating magnetic field. The
2 39 rotor winding is often of squirrelcage type with the number of poles equal to the number of poles in the stator. The currents are induced in the rotor conductivebars. The interaction of the resultant magnetic field in the airgap with the currents in the rotor conductivebars produces an electromagnetic torque, which acts on the rotor in the direction of the rotation of the magnetic field in the airgap. The performance of a threephase induction motor is analyzed based on the equivalent circuit. Because of symmetry of the three phases, a singlephase equivalent circuit is shown in Figure 3.1, it can be used to analyze the characteristics of a threephase induction motor. Figure 3.1 Equivalent Circuit of a 3 phase Induction Motor R 1 is the stator resistance, X 1 is the stator leakagereactance, comprising of stator slot leakagereactance, endwinding leakagereactance, and differential leakagereactance. X 2 and R 2 are the rotor leakagereactance and the rotor resistance, respectively. X 2 includes rotor slot leakagereactance, endring leakagereactance, differential leakagereactance, and skewslot leakagereactance. Due to the saturation phenomena in the magnetic leakage field, both X 1 and X 2 are nonlinear parameters. All the parameters in the equivalent circuit are dependent on the stator and the rotor currents. In the exciting branch, X m denotes the magnetizingreactance, and R c denotes the resistance corresponding to the ironcore losses. X m is a linearized nonlinear parameter, whose value varies with the saturation degree in the main magnetic field. Given that V 1 is the external phase voltage applied to the phase terminals, the stator phase current I 1 and the rotor current I 2, which have been
3 4 referred to the stator, can be easily computed by analysing the equivalent circuit. The equivalent circuit parameters can be derived from the following geometrical and electrical parameters: 1) Geometrical Parameters: a) Stator and Rotor diameters (inner and outer) b) Axial corelength c) Number of slots in the Stator and the Rotor d) Geometrical shapes of the Stator and the Rotor slots 2) Electrical Parameters: a) Number of Poles b) Number of conductors in series per phase c) Winding pitch d) Crosssection of the conductor e) Shortcircuited Cage ring section f) Skewing pitch of the Rotor slots These data are derived from the electromagnetic design of the machine. As shown in Figure 3.1, the actual rotor resistance R 2 and the rotor leakagereactance X 2 have to be referred to the stator using Equation (3.1) and Equation (3.2), respectively. = (3.1) = (3.2)
4 41 The coefficient K for referring the rotor parameters to the stator side is shown in Equation (3.3). N ph is the number of stator conductors in series per phase, k w1 is the statorwinding coefficient (for the airgap fundamental spatial harmonic), and N bars is the number of the squirrelcage rotor bars. (3.3) It is important to note that any statorphasewinding structure can always be described by N ph conductors in series per phase with an equivalent wire section (A wire ) suitable to carry the phase current. This means that only N ph and A wire are required for the equivalent circuit parameter computation, even if some parallel paths are used for the phasewinding realization (i.e., singlewireparallel or bobbinparallel) Stator and Rotor Resistances Equation (3.4). The stator winding resistance can be evaluated using Figure 3.2 and Figure 3.2 Length of the Averageturn of a Winding
5 42 =. (3.4) where is the resistivity of conductor material, L avg.turn is the length of the averageturn, and A wire is the crosssectional area of the wire. Equation (3.4) is quite simple in itself, but some care has to be taken to define the averageturn length. As shown in Figure 3.2, this length is the addition of two components, namely, the part of turn embedded in the slot (L core ) and the endwinding length (L ew ). Equation (3.5) to Equation (3.7) gives the length of the average turn of the conductor in the stator winding.. = 2( + ) (3.5) = (3.6) = 1 ( + ) (3.7) where D is is the inner diameter of the stator core, h s is the height of the stator slot, and k ew is the endwinding shape coefficient. The value of k ew is usually close to /2 for wirewindings, assuming a semicircumference endwinding shape with a diameter equal to w. Typically, k ew is in the range of , depending on the actual endwinding length. n r is the pitchshortening defined in number of slots, N pole is the number of poles (defined by the airgap fundamental spatial harmonic), and N ss is number of the stator slots. Assuming the number of rotor phases to be equal to the number of bars, the phaseresistance of the cage is referred to single bar and to two adjacent ring sectors, as shown in Figure 3.3. The resistance contribution of a single bar can be computed by Equation (3.8), while the resistance contribution of one Endring can be computed by Equation (3.9).
6 43 = (3.8) = (3.9) where K R is the skineffect coefficient for the bar resistance, A bar is the crosssectional area of the bar, L bar is the bar length, A a is the crosssectional area of the cagering, and D a is average diameter of the cagering. Figure 3.3 Bar and Ring Currents in Rotor Cage By using, Equation (3.8) and Equation (3.9), it is possible to compute the equivalent rotorphase resistance. As is well known, the calculation of this equivalent resistance is based on the total rotorcage joulelosses. The phasor diagram for the current is shown in Figure 3.4, where, I b is the bar current and I a as the ring current. The relationship between the ring current and the endbar current is given in Equation (3.1).
7 44 Figure 3.4 Phasor Diagram of Ring and Endbar Current (3.1) As a consequence, the total jouleloss dissipated in the rotor cage (P jr ) is defined by Equation (3.11). = + (3.11) Since each rotor bar can be considered as a phase of a multiphase winding, the equivalent rotorphase resistance is defined by Equation (3.12). = + (3.12) Classification of Magnetic Flux To calculate the inductive parameters, it is important to classify the magnetic fluxes through the machine. Figure 3.5 is used as a reference for this classification.
8 45 Figure 3.5 Fluxpath in the Machine The flux in a rotating machine can be classified into two categories: A) With respect to the fluxpath: The total flux linked ( total ) with a phase winding is the addition of two contributions, namely: 1) main, the main flux linked due to the magnetic field lines, crossing the airgap. This flux is produced simultaneously by the stator and the rotor currents. 2) local, the local flux linked due to the following two components: a) The field lines close to the conductors in the slot and the two adjacent teeth ( sl ). b) The field lines around the endwindings ( hl ). B) With reference to the energy conservation: The total flux ( total ) linked with a phase winding is the addition of the following two components:
9 46 1) useful, the linked flux that is due to the fundamental distribution of airgap flux density, and is a component of the main flux. 2) leakage, the linked flux that does not give appreciable contributions to energy conversion. With those of the above two classifications, it is possible to write the Equation (3.13) to Equation (3.15) for the total flux linked with the winding. = + (3.13) = + + (3.14) = + (3.15) As a consequence, the leakageflux in the winding is calculated using Equation (3.16). = + + (3.16) The actual speed is mainly governed by the first harmonic flux; only the fundamental flux component is conventionally considered as useful in the electromechanical energy conversion. Flux components of higher orders are considered as leakagecomponents. As a consequence, with reference to Equation (3.15), the quantity ( ) is defined as the airgap leakageflux. This airgap leakage flux is used for the calculation of the leakageinductance.
10 Leakageinductance The slot leakageinductance (both for the stator and the rotor) can be calculated on the basis of the magnetic energy stored in the slot defined by Equation (3.17). E = L I (3.17) where is the slotleakagecoefficient, L slot is the length of the winding part inside the slot, and I slot is the total current in the slot. Obviously, this current depends on the phase current (I Phase ), and on the type of phasewinding. Figure 3.6 Distribution of MagneticField in the Slot L slot is used as general symbol: It is equal to L core for the stator winding and L bar for the rotor cage. Assuming, the permeability of iron to be infinite and that the magnetic field lines are parallel into the slot as shown in Figure 3.6, the magnetic energy stored in the slot is given by Equation (3.18). = ( ) ( ) (3.18) Given the xcoordinate, the magnetic field and the slot current are calculated by using Equation (3.19) and Equation (3.2).
11 48 ( ) = ( ) ( ) ( ) (3.19) = ( ) ( ) (3.2) As a consequence, the slotleakagecoefficient is given by Equation (3.21). = ( ) ( ) (3.21) Since the permeability of iron is considered infinite, Equation (3.21) cannot be applied to closed rotor slots, because, the slot, the slotleakagecoefficient should be infinite too. In this case, taking into account the inevitable heavy saturation of the slot closing magnetic wedge, an equivalent slotopening has to be considered. Unfortunately, the selection of the width of the slotopening is not a simple task and it can be done on the basis of the actual shape of the slotclosing zone. Generally, some trialanderror steps based on the experience of the designer are required in order to obtain reasonable results. The phase slot leakageinductance can be obtained by Equation (3.22). = (3.22) Alternatively, the leakageinductance (L ) of a machine can be obtained as the sum of different leakageinductances. According to the designtradition of electrical motors, the leakageinductance (L ) can be thought of as made up of the following partial leakageinductances: Airgap leakageinductance (L g ) Slot leakageinductance (L u ) Toothtip leakageinductance (L d )
12 49 Endwinding leakageinductance (L w ) Skew leakageinductance (L sq ) The leakageinductance of the machine is the sum of these leakage inductances as shown in Equation (3.23). = (3.23) Airgap inductance is given by Equation (3.24). L o 2 v 2 kwv m Tph DL g p v v,v 1 (3.24) where µ = Permeability of vacuum m g L D = Number of phases = Airgap length = Effective corelength = Diameter of the core T ph = Number of turns per phase in a winding p = Number of polepairs = Ordinal of the harmonic k wv = Winding factor The term v, when equal to 1, in the Equation (3.24), represents the fundamental component, and thus the magnetizinginductance (L m ) of the machine. The slotinductance of a phase winding is obtained as follows:
13 5 Figure 3.7 shows the equivalent circuit of slotinductance, and its value is determined by Equation (3.25). Figure 3.7 Equivalent Circuit of SlotInductance L u = 4m Q o 2 u (3.25) where Q = Number of slots u = Permeance factor of the slot Figure 3.8 Slot Model Equation (3.26) is used to determine the permeance factor of the slot ( u ), using the dimensions of the slot model as shown in Figure 3.8.
14 51 u = h 4 3b 4 + h 3 b 4 + h 1 b 1 + h 2 b 4 b 1 ln b 4 b 1 (3.26) Toothtip leakageinductance is determined using Equation (3.27). = (3.27) d = Permeance factor of toothtip Endwinding leakageinductance (L w ) calculation is given by Equation (3.28) = (3.28) l w = Average length of the endwinding w = Permeance factor of endwinding q = Number of slots per pole per phase Equation (3.29) shows the Skew leakageinductance (L sq ) = (3.29) where =, the Leakage factor caused by skewing k sq = skewing factor =
15 CALCULATION OF PERFORMANCE PARAMETERS The magnetic energy stored in a slot can be calculated by using any one of the Flux analysis softwares, namely, 2D, RMxprt, and MotorPro, after completion of the initial design using lowloss materials. The magnetic circuit of the motor is constituted by the lamination of the stator, the rotor, and the airgap. The energy conversion is assisted by the flux in the airgap, driven by magnetomotiveforce (mmf) produced in the stator winding. The mmf required to drive the flux is influenced by the reluctance of the magnetic circuit. The reluctance of the magnetic circuit is determined by the length and the relative permeability of the material as given in Equation (3.3). = (3.3) where S = Reluctance = Length of the magnetic circuit = Permeability of free space = Relative permeability A = Area of the magnetic circuit The mean length of the magnetic circuit is influenced by the shape of the slot and the airgap. Material composition of stamping influences the relative permeability and the saturation factor coefficient. Reduced reluctance circuit needs less mmf to force the flux, and hence results in less magnetizing current. Hence, the output power, power factor, and efficiency improve significantly. This could be understood from the equivalent circuit shown in Figure 3.1, and Equation (3.31) to Equation (3.37). The electromagnetic power (P m ), otherwise called as the airgap power, is determined by Equation (3.31). = 3 (3.31)
16 53 The electromagnetic torque (T m ) is calculated using Equation (3.32). = (3.32) where, denotes the synchronous speed in rad/s. Equation (3.33) gives the mechanical shaft output torque (T sh ). = (3.33) where, T fw denotes the frictional and windage torque. The output power (P o ) is shown in Equation (3.34). = (3.34) where r = (1 s) denotes the rotor speed in rad/s. Equation (3.35) is used to calculate the input power to the motor (P i ). = (3.35) where P fw, P rc, P cl, P sc, and P l denote the frictional and windage losses, the rotor copper loss, the ironcore loss, the stator copper loss, and the stray loss, respectively. The power factor is determined by Equation (3.36). = (3.36) Equation (3.37) is used to determine the efficiency. = 1 (3.37)
17 ANALYSIS USING ROTATIONAL MACHINE EXPERT Rotational Machine Expert (RMxprt) is an interactive software package from ANSOFT Corporation used for the design and analysis of electrical machines. When a new project is started in RMxprt, the type of motor is to be selected. The parameters associated with the selected machine are given as input in the property window. The property windows are accessed by clicking each of the machine elements; for example, stator, rotor, and shaft under machine in the project tree. Solution and output options such as the rated output, torque, and load current, etc., are set by adding a solutionsetup in analysis of the project tree. A 3phase, 38 V, 2pole submersible induction motor with the power range 3HP to 7.5HP has been chosen, based on the market requirement. (Source: TEXMO Industries, CRI Pumps, DECCAN Industries, and PSG Industrial Institute). Different stator, rotor slotshapes have been considered for optimisation. The stator and rotor slotmodels used for simulation are shown in Figure 3.9 and Figure 3.1, respectively. Figure 3.9 Stator Slotmodels used for Optimisation
18 55 Figure 3.1 Rotor Slotmodels used for Optimisation The various dimensions of slots pertaining to Stator and Rotor are shown in Table 3.1 and Table 3.2, respectively. Table 3.1 Dimensions of Stator Slots Dimension (mm) Slot Type B S B S1 B S2 H S H S1 H S2 R S1 R S2 A B C D E F Table 3.2 Dimensions of Rotor Slots Dimension (mm) Slot Type B S B S1 B S2 H S H S1 H S2 R S
19 56 All the design values related to each section as mentioned in Figure 3.11 have been configured in the software, namely, machine type, main dimensions, material characteristics, BH and BPcurves for the stamping, type of shaft material (SS37), and body material (cast iron, aluminium, and SS34). The basic process in RMxprt is illustrated with the help of the flowchart in Figure Start Define Data for 3phase Induction Motor General Data Stator Data Rotor Data Solution Data Machine type No. of Poles Stray loss Friction loss Windage loss Reference speed Outer diameter Inner diameter Length Type of Steel Stacking factor No. of slots SlotModel Slot dimensions Winding details Outer diameter Inner diameter Length Type of Steel Stacking factor No. of slots SlotModel Slot dimensions Winding details Skew width Rotor type Dutycycle Type of Load Rated output Rated voltage Rated speed Operating temperature Winding connection Frequency Analysis of Machine Add a solution setup Validation check Analyse Design Output of Machine Design sheet Performance table Performance curves Figure 3.11 Flowchart for Basic Process in RMxprt The iterations have been performed, using the optimetrics tool shown in Figure 3.12, by choosing different combinations of corelength, number of turns per phase, and magnetic loading for 3phase, 5HP, 38 V submersible induction motor.
20 57 Start RMxprt Model (initial design) Define design variables and its range of values Add parametric setting Define performance attributes needed for calculation Analyse Apply optimum result for initial design RMxprt Model (optimised design) Figure 3.12 Flowchart for Optimetrics Tool in RMxprt Table 3.3 to Table 3.8 show the results obtained from the simulation for different slotmodel combinations. The parameters that influence the magnetic circuit, namely, Stator Leakagereactance, Magnetizingreactance, Rotor Leakagereactance, Resistance corresponding to Ironcore Loss, Stator Phase Current, and Magnetizing Current have been considered for the selection of optimum slotmodel.
21 58 Table 3.3 Parameters for SlotA Combination Parameters Slot1 Slot2 Slot3 Slot4 Stator Leakagereactance ( ) Magnetizingreactance ( ) Rotor Leakagereactance ( ) Resistance Corresponding to Ironcore Loss ( ) Stator Phase Current (A) Magnetizing Current (A) Table 3.4 Parameters for SlotB Combination Parameters Slot1 Slot2 Slot3 Slot4 Stator Leakagereactance ( ) Magnetizingreactance ( ) Rotor Leakagereactance ( ) Resistance Corresponding to Ironcore Loss ( ) Stator Phase Current (A) Magnetizing Current (A) Table 3.5 Parameters for SlotC Combination Parameters Slot1 Slot2 Slot3 Slot4 Stator Leakagereactance ( ) Magnetizingreactance ( ) Rotor Leakagereactance ( ) Resistance Corresponding to Ironcore Loss ( ) Stator Phase Current (A) Magnetizing Current (A)
22 59 Table 3.6 Parameters for SlotD Combination Parameters Slot1 Slot2 Slot3 Slot4 Stator Leakagereactance ( ) Magnetizingreactance ( ) Rotor Leakagereactance ( ) Resistance Corresponding to Ironcore Loss ( ) Stator Phase Current (A) Magnetizing Current (A) Table 3.7 Parameters for SlotE Combination Parameters Slot1 Slot2 Slot3 Slot4 Stator Leakagereactance ( ) Magnetizingreactance ( ) Rotor Leakagereactance ( ) Resistance Corresponding to Ironcore Loss ( ) Stator Phase Current (A) Magnetizing Current (A) Table 3.8 Parameters for SlotF Combination Parameters Slot1 Slot2 Slot3 Slot4 Stator Leakagereactance ( ) Magnetizingreactance ( ) Rotor Leakagereactance ( ) Resistance Corresponding to Ironcore Loss ( ) Stator Phase Current (A) Magnetizing Current (A)
23 6 It could be concluded from the parameters in Table 3.3 to Table 3.8 that the combination of SlotA type stator slot with Slot2 type rotor slot contribute to a good magnetic circuit. The advantages of this combination are: Reduced Stator and Rotor Leakagereactances Increased Magnetizingreactance Increased Resistance corresponding to IronCore Loss Reduced Stator Phase Current Reduced Magnetizing Current The output power of the underwater motor can be increased by reducing the magnetizing current. Reduced magnetizing current will improve the operating power factor. A cumulative operation of more number of such motors will lead to energysaving and the load factor of the connected distribution transformer will come down, resulting in good voltage regulation and high Transformer utilization factor. Existing SlotD type stator slot and Slot1 type rotor slot combination shown in Figure 3.13a are compared with the proposed SlotA type stator slot and Slot2 type rotor slot shown in Figure 3.13b. Submersible motors with the ratings of 3HP, 5HP, 6HP, and 7.5HP have been considered for optimisation.
24 61 (a) (b) Figure 3.13 Stamping Models (a) SlotD Type Stator and Slot1 Type Rotor (b) SlotA Type Stator and Slot2 Type Rotor For analysis in RMxprt, a 3phase, 38 V, 2pole, 5 Hz, and starconnected submersible induction motor type has been considered with the specifications given in Table 3.9. Table 3.9 Specifications of the Motors S. No. Parameter 3HP 5HP 6HP 7.5HP 1 Outer diameter of the Stator (mm) Inner Diameter of the Stator (mm) Length of the Stator core (mm) Airgap (mm) Inner diameter of the Rotor (mm) EndRing Width (mm) EndRing Length (mm) EndRing Height (mm) Number of Stator Slots Number of Rotor Slots Conductors per slot
25 62 The stator and rotor stampings are common for the selected range of motors. M43_29Ggradestamping has been used for both the stator and the rotor. The corelength has been varied based on the power rating of the motor, the magnetic loading, and the electric loading values are adjusted to optimize the corelength and other performance parameters. The electric loading value is kept slightly higher for the submersible motor compared to the normal industrytype motor because of the forcedwater cooling. The number of conductors per slot and EndRing width have also been changed so as to meet the design requirements. 3.5 SIMULATION RESULTS With fixed operating conditions, the machines have been simulated in RMxprt and the results are tabulated as shown in Table 3.1 and Table Following inferences could be made from Table 3.1 and Table 3.11: The leakagereactance of stator and rotor, namely, Slot, Endwinding, Differential, and Skewing Leakagereactance values have got reduced. Increased values of Ironcore Loss Resistance and Magnetizingreactance reduce the losscomponent current and the magnetizing current, resulting in improvement of the operating power factor. The stator phase current of the proposed slot type motor is less, when compared to that of the existing slot type motor. There is a significant improvement in the efficiency of the motor with the proposed slotshape.
26 63
27 64
28 65 (a) (b) Figure 3.14 Flux Distribution (a) Existing Slot (b) Proposed Slot Flux distribution in the Motor is shown in Figure The flux density with the proposed stator slot is found to be from 1.22 Tesla to 1.55 Tesla; but in the existing stator, it is from 1.2 Tesla to 1.7 Tesla. Since the magnetic flux density is less in the proposed slot, there is a reduction in the required magnetizing current. 3.6 REALTIME IMPLEMENTATION AND RESULTS The stampings and the test setup are shown in Figure 3.15 and Figure 3.16, respectively.
29 66 (a) (b) Figure 3.15 Stampings (a) Existing (b) Proposed (a) (b) Figure 3.16 Test Setup (a) Testing Panel (b) Pump Loading The performance test reports for 3HP, 5HP, 6HP, and 7.5HP pumpsets, with the existing and the proposed motor slotshape are shown in Table 3.12 to Table 3.19.
30 67 Table 3.12 Performance Test of 3HP Submersiblepumpset with the Existing slotshape S.No. Speed (rpm) Delivery gauge reading (Kgf/cm 2 ) Total head (m) Rise in Tank (cm) Time for rise (s) Input Discharge Current Power (lpm) (A) (kw) Pump output (kw) Overall efficiency (%) Table 3.13 Performance Test of 3HP Submersiblepumpset with the Proposed slotshape S.No. Speed Delivery gauge reading (rpm) (Kgf/cm 2 ) Total head (m) Rise in Tank (cm) Time for rise (s) Discharge (lpm) Current (A) Input Power (kw) Pump output (kw) Overall efficiency (%)
31 Head (m) Overall Efficiency (%) Current (A) Motor Input (kw) Discharge (lps) (a) Head (m) Overall Efficiency (%) Current (A) Motor Input (kw) Discharge (lps) (b) Figure 3.17 Pump Performance Curve: 3HP (a) Existing (b) Proposed
32 Current in the Proposed Design (A) Discharge in the Existing Design (lpm). Current in the Existing Design (A) Discharge in the Proposed Design (lpm) Delivery Gauge Reading (kgf/cm 2 ) (a) Current in the Existing Design (A) pf in the Existing Design. Current in the Proposed Design (A) pf in the Proposed Design Delivery Gauge Reading (kgf/cm 2 ) (b) Figure 3.18 Performance Comparison Curve: 3HP (a) Discharge and Current (b) Current & Power factor
33 7 Table 3.14 Performance Test of 5HP Submersiblepumpset with the Existing slotshape S.No. Speed (rpm) Delivery gauge reading (Kgf/cm 2 ) Total head (m) Rise in Tank (cm) Time for rise (s) Discharge (lpm) Current (A) Input Power (kw) Pump output (kw) Overall efficiency (%) Table 3.15 Performance Test of 5HP Submersiblepumpset with the Proposed slotshape S.No. Speed (rpm) Delivery gauge reading (Kgf/cm 2 ) Total head (m) Rise in Tank (cm) Time for rise (s) Discharge (lpm) Current (A) Input Power (kw) Pump output (kw) Overall efficiency (%)
34 Head (m) Overall Efficiency (%) Current (A) Motor Input (kw) Discharge (lps) (a) Head (m) Overall Efficiency (%) Current (A) Motor Input (kw) Discharge (lps) (b) Figure 3.19 Pump Performance Curve: 5HP (a) Existing (b) Proposed
35 Current in the Proposed Design (A) Discharge in the Existing Design (lpm). Current in the Existing Design (A) Discharge in the Proposed Design (lpm) Delivery Gauge Reading (kgf/cm 2 ) (a) 15 1 Current in the Existing Design (A) pf in the Existing Design. Current in the Proposed Design (A) pf in the Proposed Design Delivery Gauge Reading (kgf/cm 2 ) (b) Figure 3.2 Performance Comparison Curve: 5HP (a) Discharge and Current (b) Current and Power factor
36 73 Table 3.16 Performance Test of 6HP Submersiblepumpset with the Existing slotshape S.No. Speed (rpm) Delivery gauge reading (Kgf/cm 2 ) Total head (m) Rise in Tank (cm) Time for rise (s) Discharge (lpm) Current (A) Input Power (kw) Pump output (kw) Overall efficiency (%) Table 3.17 Performance Test of 6HP Submersiblepumpset with the Proposed slotshape S.No. Speed (rpm) Delivery gauge reading (Kgf/cm 2 ) Total head (m) Rise in Tank (cm) Time for rise (s) Discharge (lpm) Current (A) Input Power (kw) Pump output (kw) Overall efficiency (%)
37 Head (m) Oveall Efficiency (%) Current (A) Motor Input (kw) Discharge (lps) (a) Head (m) Oveall Efficiency (%) Current (A) Motor Input (kw) Discharge (lps) (b) Figure 3.21 Pump Performance Curve: 6HP (a) Existing (b) Proposed
38 75 Current in the Existing Design (A) Discharge in the Existing Design (lpm) Current in the Proposed Design (A) Discharge in the Proposed Design (lpm) Delivery Gauge Reading (kgf/cm 2 ) (a) 1 Current in the Existing Design (A) pf in the Existing Design Current in the Proposed Design (A) pf in the Proposed Design Delivery Gauge Reading (kgf/cm 2 ) (b). Figure 3.22 Performance Comparison Curve: 6HP (a) Discharge and Current (b) Current and Power factor
39 76 Table 3.18 Performance Test of 7.5HP Submersiblepumpset with the Existing slotshape S.No. Speed (rpm) Delivery gauge reading (Kgf/cm 2 ) Total head (m) Rise in Tank (cm) Time for rise (s) Discharge (lpm) Current (A) Input Power (kw) Pump output (kw) Overall efficiency (%) Table 3.19 Performance Test of 7.5HP Submersiblepumpset with the Proposed slotshape S.No. Speed (rpm) Delivery gauge reading (Kgf/cm 2 ) Total head (m) Rise in Tank (cm) Time for rise (s) Discharge (lpm) Current (A) Input Power (kw) Pump output (kw) Overall efficiency (%)
40 77 Head (m) Overall Efficiency (%) Current (A) Motor Input (kw) Discharge (lps) (a) Head (m) Overall Efficiency (%) Current (A) Motor Input (kw) Discharge (lps) (b) Figure 3.23 Pump Performance Curve: 7.5HP (a) Existing (b) Proposed
41 78 Current in the Proposed Design (A) Discharge in the Existing Design (lpm) (a) Current in the Existing Design (A) Discharge in the Proposed Design (lpm) Delivery Gauge Reading (kgf/cm 2 ) Current in the Existing Design (A) pf in the Existing Design Current in the Proposed Design (A) pf in the Proposed Design Delivery Gauge Reading (kgf/cm 2 ) (b) Figure 3.24 Performance Comparison Curve: 7.5HP (a) Discharge and Current (b) Current and Power factor
42 79 Performance Comparison Curves for 3HP, 5HP, 6HP, and 7.5HP, Pumpsets have been depicted in Figure 3.17 to Figure From the performance curves, the following inferences have been made: The current drawn from the supply gets reduced by 1 to 1.7 A, and the power factor has also got significantly improved. Input power consumed by the pumpset gets significantly reduced by 13 to 3 W. There is an increase in speed of the pumpset by 15 to 3 rpm, and this results in increase in the discharge of water by 3 to 7 lpm. The overall efficiency of the pumpset has gone up by 3 to 7 %. Therefore, the adoption of these motors in the agriculture field can give immense benefits to the user, as well as to the country and the global environment at large.
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