# Low-Head Energy Conversion: A Conceptual Design and Laboratory Investigation of a Microtubular Hydro Propeller

Authors: Helena M. Ramos; Mariana Simão; Kaloyan N. Kenov
Journal: ISRN Mechanical Engineering
 (2012)

---

## Abstract

Low-head microhydro systems for energy production are becoming accepted because of oil crises and new advances in their design and efficiencies. As this is still a new area for development and experimentation, it is important to test and validate the optimal conditions and the hydrodynamic behaviour of such systems under different conditions. The aim of this paper is to present a turbine design validation practise, which researchers and equipment manufactures can use for the hydrodynamic behaviour analysis of new low-head turbines prior to production and application. Laboratory experimental tests and advanced CFD numerical analysis are described for the flow behaviour analysis of a new prototype microtubular propeller. Laboratory experimental results are presented and used for the evaluation of the turbine performance curves. Comparisons between experimental and CFD results are also presented. Finally, an assessment of the hydrodynamic behaviour is made for a scaled model application, using the theory of turbomachine similarity.


---

## Body

## 1. Introduction

Despite that researchers and equipment manufactures have paid less attention to the emerging field of low-head power engines, microturbines can provide innovative, environmental friendly, and cost-effective solutions for energy production. The challenge is to provide new turbine designs, which can be customized and applied to existing water systems, characterized by low-head and nearly constant flow rates.Microhydropower, generally, refers to power below 5 kW. Blakely and O’Connor [1] and, most recently, Campbell [2] has reported technologies, prospects, and potential uses of micro-hydro-electric schemes in remote locations. Howey [3] built and tested a fixed geometry propeller turbine for a runner speed of 1000 rpm, suited up to a 35 m head, and at about a 5 l/s flow rate, documenting good efficiencies. Simpson and Williams [4] also designed and field-tested a fixed geometry propeller turbine with a spiral casing, showing an overall mechanical efficiency of 65%. Several researchers (Demetriades [5], Upadhyay [6], Alexander et al. [7–10], and, most recently, Skotak et al. [11]) have developed medium-sized models of propellers turbines.Olgun [12, 13] investigated the performance of a crossflow turbine as a source of hydropower generation for small and microsystems, especially for low-head establishments. Sumathy et al. [14] presented analysis of the operation and performance of a solar thermal water pump. Krishnamoorthy et al. [15] reported design optimization studies conducted on a novel steam-operated pistonless pump, fuelled by biomass. Sutikno and Adam [16] presented research on the design, simulation, and experimental work of a very low-head turbine. Kaniecki and Krzemianowski [17] reported the complete design process for a low-head propeller hydraulic turbine.Until now, very few to no studies have been conducted for propellers working as microturbines, especially for solutions working under low-power rates particularly designed to be implemented in existing water pipes through a bypass to the system (e.g., in water supply systems), allowing for new developments and improvements in their design, efficiency, size, and stability of operation. The design solutions found in literature are usually appropriate for hydropower schemes with large discharge values. Smaller and optimized blade geometries, applied to low-power flow, especially associated with water pipe systems, are still underrepresented in literature and in particular in practise.According to Ramos et al. [18], the behaviour of such microhydro converters can differ depending on the flow conditions and on the runner configuration, particularly, on the inlet and outlet flow and on the shape of the blades. The design of new low-head devices cannot be solely based on a large turbine scaling-down methodology. To overcome this limitation, CFD analysis can be used to provide design and hydrodynamic behaviour information, which can strongly support the experimental tools. CFD analysis is important to help in the design of the best configuration for different system’s characteristics and flow scenarios, according to Rawal and Kshirsagar [19].This paper aims to close the existing gap found in literature on how to obtain the optimal design of low-power turbines. Focus is put on a methodology and on a new design, which couples together mathematical modelling, CFD numerical analysis, and laboratory testing in order to validate the optimal performance of a new microtubular low-head converter. This is an important topic because water supply and distribution management systems are interested in this solution, and as this new class of low-head converters can be implemented as decentralized solutions in pressurized water pipe infrastructures (e.g., in water supply, irrigation and waste water, or drainage systems) in rural and remote areas for alternative and low-cost energy production.


## 2. Turbine Design

To determine optimal design results, which to lead to the best-efficiency point (BEP) of a prototype turbine, it is important to analyse different blade slopes (i.e., angle variation) when designing the impeller blades. The thickness of the impeller blades should also be observed to avoid disturbances into the flow, which can cause additional losses, and may constrain the overall efficiency. A maximum thickness of 1 mm was considered in this study, in order to avoid limitations in the CFD mesh created for the model simulations.Figure1 shows the velocity triangles associated with the optimization of the blade configuration. It also shows the parameters related to each other from the direction of the blade profiles, such as the angle variation, as indicated by the vectors. A blade model configuration (BMC) was developed to estimate the best blade orientation, which to lead to best efficiency operating conditions, as reported by Ramos et al. [20]. The proper blades orientation is a computationally and experimentally demanding process, which requires attention and performance of sensitivity analysis for different characteristic parameters associated with the inlet and outlet velocity triangles. Figure 1 also identifies the vectors of absolute (v), periphery (c), and relative runner blade velocity (u). Essential relationships are established among them to calculate the turbine discharge for a given configuration. The periphery velocity (c) at the inlet and outlet of a blade, which depends on the impeller rotational speed (ω) and on the blade radius (r), can be obtained by  (1)(1)c1=c2=ωr,
and the absolute velocity (v) depends on the discharge (Q) which passes through the impeller, given by  (2)(2)v1=v2s=QS=Qπ(re2-ri2),
where S is the tubular cross-section area, and re and ri are the tip and hub blade radius between the runner periphery and internal bulb, respectively.Figure 1
Velocity vectors in a blade of a turbine propeller.The blade angles (α1 and α2) on the periphery of the inlet and outlet (subscript 1 and 2, resp.) yield the following (3):(3)tgα1=v1c1=QS⋅1ωr,tgα2=v2sc2+v2t=v1ωr+v2t⟺tgα2=QS(1ωr+v2t).Analysis of the flow at downstream of the impeller reveals a vortex formation (k), which depends on the radius of the blade, the flow cross-section and on the discharge value as presented in  (4)(4)v2t=kr⟹k=-ωr+QrStgα2.As the blade angle changes from the inlet to the outlet, between the upstream turbine section, where the flow impulses the blade, to the downstream turbine section, where the flow exits the machine, the overall efficiency changes. This may lead to better performance, depending on the angular variation along the blade profile. Based on (3) to (4), the BMC establishes the slope blade variation for a given rotational speed, leading to an optimum performance.Using (4) and values for head, discharge, rotational speed, and runner diameter, the relationship between the runner bulb and periphery diameter, the open blade angle (ap) (see Figure 2), which depends on the number of blades, the angles of the inlet and outlet from the axis to the periphery in each blade, can be calculated. It is also possible to calculate the power, the specific speed, and the constant vortex velocity. Having data from the input conditions, the correct blade configuration from the bulb section to the periphery (Figure 3) is then determined.Scheme of a propeller: (a) plan view and five profiles in a blade and (b) parameters associated to the tracing profiles in each blade.
(a)(b)Figure 3
Design of different profiles for each blade. Impeller configuration.Torque (M), impeller rotational speed, fluid mass density (ρ), discharge, and free-vortex constant are used to calculate the engine or mechanical power (Pmec), by using (5),(5)Pmec=Mω=ρQkω,
the hydraulic power (Ph) is obtained by using the specific weight of the fluid (γ), the discharge, and the net head (H) in (6),(6)Ph=γQH,
and the efficiency (ηt) can be obtained by (7), using the mechanical and the hydraulic power
(7)ηt=PmecPh=ρQkωγQH=kωgH.Outer impeller diameter of 100 mm, with a bulb diameter of 50 mm, is considered for the design of this small-scale tubular propeller. This propeller design is adequate for laboratory testing and for the most of real water distribution system conditions with small flow discharge. According to Table1, the blades design is built to operate with a discharge around 5 l/s and at a maximum rotational speed of 300 rpm. To design the blades profile, presented in Figure 3, the variables presented in Table 1 are used in (3) to (6).Table 1
Values for the blade profile configuration.
r (m)tg(a1)tg(a2)L (m)rh (m)x1 (m)x2 (m)xc (m)yc (m)P10.02500.86460.29750.03540.09580.0177−0.0177−0.04500.07250.02810.76850.30660.03980.12580.0199−0.0199−0.05680.0997P20.03130.69170.31160.04420.16280.0221−0.0221−0.07050.13390.03440.62880.31310.04860.20820.0243−0.0243−0.08650.1762P30.03750.57640.31200.05300.26320.0265−0.0265−0.10490.22800.04060.53210.30900.05750.32920.0287−0.0287−0.12590.2907P40.04380.49410.30450.06190.40800.0309−0.0309−0.14980.36580.04690.46110.29900.06630.50110.0331−0.0331−0.17670.4551P50.05000.43230.29280.07070.61040.0354−0.0354−0.20690.5603


## 3. Experimental Tests

In order to maintain a continuous steady-state flow conditions, an experimental loop pipe system was developed for the analysis of the flow through a prototype of a micro-propeller turbine with the impeller diameter ofD=100 mm. This setup consists of a pressure pipe system with an installed pump for recirculation, an air vessel for upstream pressure control, an electromagnetic flow meter, and a downstream reservoir with a triangular (90°) weir. A valve is used for flow control. When the valve is fully open, the maximum possible turbine flow is 5.2 l/s.In order to estimate the output power, the shaft transmits the momentum to a torque balance through the turbine upstream curve. During testing, isotropic behaviour of the flow upstream of the turbine was observed. Observed were also few anisotropic occurrences through the impeller, influenced by the flow rotation and separation flow zone of the boundary layer, which exists downstream of the internal impeller bulb (as presented in Figure6).Under laboratory conditions, the best efficiency point (BEP) for the micro-tubular propeller (D=100 mm) was estimated at about 70% for a rotational speed of 200 rpm (Nsqt (specific rotational speed) = 84 rpm (m, m3/s) based on (10)), as shown in Figure 4. The performance dimensionless curves are based on efficiency (from (7)), the head number, and discharge number, defined asFigure 4
Characteristics curves of the micro-tubular propeller.Discharge number (φ):
(8)φ=QND3Head number (Ψ):
(9)ψ=gHN2D2,
where N is the rotational speed, and D is the pipe diameter or outside diameter of the blades.Under laboratory conditions, experimental results are obtained by regulating the discharge control valve, measuring the runner speed, with a tachometer Hibok-24 for different flow values, the discharge and head, in an electromagnetic flow meter and in pressure transducers at upstream and downstream of the turbine, in undisturbed flow zones. Using an ultrasonic Doppler velocimetry (UDV) in the turbine system (Figure5), the velocity profiles were analysed. With the UDV sample placed in a vertical-sloped position of 25°, this device was used for the evaluation of the flow hydrodynamic behaviour in real-time situation. Figures 6 and 7 show different velocity profiles along the runner boundary layer, where the behaviour of the flow separation zone is represented, and in which the velocity profile inversion tendency is visible. The most important features during the identification of instantaneous flow velocity values and mean profiles (Figure 7) are due to: (a) flow irregularity which is indicated by the occurrence of three-dimensional vorticity fluctuations, that is, the turbulent movements are of the rotational type, (b) energy dissipation, that is, the turbulent phenomenon is associated with a significant energy loss, where the turbulence is damped quickly by giving a greater homogeneity and isotropy to the flow motion, (c) diffusivity, corresponding to a rapid mixing within the fluid domain, followed by transfer of momentum, heat and mass, in rapid variations or fluctuations in the flow.Figure 5
Experimental facility of the micro-tubular propeller: UDV (left), balance torque (center), and rotational speed measurement (right).Separation of the boundary layer and velocity profiles.
(a)(b)Flow velocity profiles obtained by UDV along the turbine: (a) at upstream in the nonpropeller disturbed zone, (b) at the upstream shaft, (c) in the middle of the impeller, (d) at downstream of the impeller.
(a)(b)(c)(d)


## 4. Numerical Modelling

### 4.1. Performance Curves

Comparisons between BMC and 3D-CFD simulations were developed for an impeller design with four blades, characterised by the specific speed, as stated in(10)(10)Nsqt=NQH0.75.From Table2 it is possible to confirm the good match between the BMC (maximum theoretical efficiency of 100%) and the 3D-CFD simulations, even with existing losses, turbulence effects, anisotropy in the zones of high flow circulation, and scale effects, which are not considered neither in the theoretical methodology for BMC or in CFD analyses. CFD simulation use, in the first stage, angles obtained by BMC, but a further investigation of the best-efficiency operating conditions require small corrections to these angles, as shown in Table 2.Table 2
Comparisons between BMC and CFD for the tip and hub angles.
MethodologyCharacteristic parametersBMCCFDD=100mmD=200mmD=100mmD=200mmNsqt=80rpmNsqt=77rpmInlet hub angle (α1) (°)414630Outlet hub angle (α2) (°)171130Inlet tip angle (α1) (°)232425Outlet tip angle (α2) (°)161425Power (W)4.799674.29869It is also worth mentioning the difference in power values between impellers with diameters of 100 and 200 mm due to essentially differences in the flow values. Two geometrically similar turbines operating at rotational speeds, which satisfy the condition presented in (11), usually have different efficiency values, in particular when the relationship between the homologous lengths is high.(11)NN′=(HH′)1/2D′D.
The difference in efficiency values is caused by scale effects, driven by the effect of viscosity, which causes loss of pressure, thus preventing a quadratic variation of the flow velocity.In the micro-tubular propeller ofD=200 mm, the efficiency (Figure 8) is then obtained for different rotational speed values and flow conditions. Figure 8 also shows the curves of head and mechanical power versus discharge, and Figure 9 shows the performance curves for head and efficiency versus discharge number variation for the micro-tubular propeller with D=100 mm tested in laboratory.Performance curves for a runner diameter of 200 mm: (a) efficiency and head versus rotational speed and (b) head and mechanical power versus discharge.
(a)(b)Figure 9
Comparison of power and head numbers and efficiency versus discharge number for different rotational speeds withD=100 mm.


### 4.2. Hydrodynamic Behaviour

Once the BEP was established for the micro-tubular propeller based on mathematical modelling through the BMC model and CFD simulations, a detailed analysis was developed in order to better understand the 3D hydrodynamic behaviour of the flow throughout the impeller, as documented by Scott-Pomerantz [21]. Corresponding flow velocities, total pressure, and wall shear stress are presented in Figure 10, for the micro-tubular propeller tested in laboratory (D=100 mm). This 3D fluid-computational analysis considers steady-state pressurized flow conditions, keeping a constant rotational speed, where the singularities reflect an increase of turbulence. Analysis of the same figure shows flow disturbances inside the turbine. This is not only due to the rotation of the impeller, as it is associated to the circulation flow, but also to the way in which the flow enters into the turbine section, going through the propeller and leaving with a rotational movement (in a vortex configuration) towards the draft tube. Upstream of the turbine, the flow has a low velocity and higher-pressure values, exhibiting an irrotational behaviour. At the turbine section the flow is influenced by the impeller contour, which induces a flow separation effect which significantly affects the turbulence, as reflected by the wall shear stress. It is also noticed that the shear stress is higher near the periphery of the blades, inducing a significant flow resistance in this zone.Fluid behaviour inside the micro-tubular propeller.
(a)(b)(c)For this micro-tubular turbine design, four sectioning plans (Figure11) are used to analyse the behaviour of the flow in zones where the flow range can vary and where a better understanding about its behaviour is needed. In Figure 12, the fluid enters the turbine with an average speed of 0.52 m/s, which decreases as the flow approaches the tubular walls due to the effect caused by wall friction. As it approaches the curve and the impeller, the flow exhibits a nonlinear behaviour in the velocity distribution. Along the axis, the flow tends to be influenced by the shaft rotation, which induces the formation of separation zones. The sectioning plans along the turbine allow the confirmation and visualization of the flow behaviour occurring through the propeller.Figure 11
Schematic representations of the sectioning plans for instantaneous velocity analysis.CFD simulations for the flow velocity variation across the turbine.
(a)(b)(c)(d)


## 4.1. Performance Curves

Comparisons between BMC and 3D-CFD simulations were developed for an impeller design with four blades, characterised by the specific speed, as stated in(10)(10)Nsqt=NQH0.75.From Table2 it is possible to confirm the good match between the BMC (maximum theoretical efficiency of 100%) and the 3D-CFD simulations, even with existing losses, turbulence effects, anisotropy in the zones of high flow circulation, and scale effects, which are not considered neither in the theoretical methodology for BMC or in CFD analyses. CFD simulation use, in the first stage, angles obtained by BMC, but a further investigation of the best-efficiency operating conditions require small corrections to these angles, as shown in Table 2.Table 2
Comparisons between BMC and CFD for the tip and hub angles.
MethodologyCharacteristic parametersBMCCFDD=100mmD=200mmD=100mmD=200mmNsqt=80rpmNsqt=77rpmInlet hub angle (α1) (°)414630Outlet hub angle (α2) (°)171130Inlet tip angle (α1) (°)232425Outlet tip angle (α2) (°)161425Power (W)4.799674.29869It is also worth mentioning the difference in power values between impellers with diameters of 100 and 200 mm due to essentially differences in the flow values. Two geometrically similar turbines operating at rotational speeds, which satisfy the condition presented in (11), usually have different efficiency values, in particular when the relationship between the homologous lengths is high.(11)NN′=(HH′)1/2D′D.
The difference in efficiency values is caused by scale effects, driven by the effect of viscosity, which causes loss of pressure, thus preventing a quadratic variation of the flow velocity.In the micro-tubular propeller ofD=200 mm, the efficiency (Figure 8) is then obtained for different rotational speed values and flow conditions. Figure 8 also shows the curves of head and mechanical power versus discharge, and Figure 9 shows the performance curves for head and efficiency versus discharge number variation for the micro-tubular propeller with D=100 mm tested in laboratory.Performance curves for a runner diameter of 200 mm: (a) efficiency and head versus rotational speed and (b) head and mechanical power versus discharge.
(a)(b)Figure 9
Comparison of power and head numbers and efficiency versus discharge number for different rotational speeds withD=100 mm.


## 4.2. Hydrodynamic Behaviour

Once the BEP was established for the micro-tubular propeller based on mathematical modelling through the BMC model and CFD simulations, a detailed analysis was developed in order to better understand the 3D hydrodynamic behaviour of the flow throughout the impeller, as documented by Scott-Pomerantz [21]. Corresponding flow velocities, total pressure, and wall shear stress are presented in Figure 10, for the micro-tubular propeller tested in laboratory (D=100 mm). This 3D fluid-computational analysis considers steady-state pressurized flow conditions, keeping a constant rotational speed, where the singularities reflect an increase of turbulence. Analysis of the same figure shows flow disturbances inside the turbine. This is not only due to the rotation of the impeller, as it is associated to the circulation flow, but also to the way in which the flow enters into the turbine section, going through the propeller and leaving with a rotational movement (in a vortex configuration) towards the draft tube. Upstream of the turbine, the flow has a low velocity and higher-pressure values, exhibiting an irrotational behaviour. At the turbine section the flow is influenced by the impeller contour, which induces a flow separation effect which significantly affects the turbulence, as reflected by the wall shear stress. It is also noticed that the shear stress is higher near the periphery of the blades, inducing a significant flow resistance in this zone.Fluid behaviour inside the micro-tubular propeller.
(a)(b)(c)For this micro-tubular turbine design, four sectioning plans (Figure11) are used to analyse the behaviour of the flow in zones where the flow range can vary and where a better understanding about its behaviour is needed. In Figure 12, the fluid enters the turbine with an average speed of 0.52 m/s, which decreases as the flow approaches the tubular walls due to the effect caused by wall friction. As it approaches the curve and the impeller, the flow exhibits a nonlinear behaviour in the velocity distribution. Along the axis, the flow tends to be influenced by the shaft rotation, which induces the formation of separation zones. The sectioning plans along the turbine allow the confirmation and visualization of the flow behaviour occurring through the propeller.Figure 11
Schematic representations of the sectioning plans for instantaneous velocity analysis.CFD simulations for the flow velocity variation across the turbine.
(a)(b)(c)(d)


## 5. Comparisons and Results Discussion

Comparing Figure7 (experiments) with Figure 12 (CFD simulations), a similar behaviour of the fluid is evident, as well as the identification of the section in which the separation effect is more significant. When the fluid comes closer to the curve where the turbine shaft is located, there is certain anisotropy with velocity retardation induced by the impeller rotation. Once the flow passes through the bulb, pressure and velocity decrease, induced by the sub-pressure existing downstream of the impeller. This leads to the formation of a turbulent wake zone, as established by Ramos et al. [22]. Along the turbine the fluid moves into two regions: (1)a thin layer near the solid walls, in which the tangential stress play is an important role (the boundary layer); and (2) the remaining part is fullfilled where the shear stress is less significant.Dimensionless characteristic parameters of CFD simulations and laboratory tests were selected and compared as shown in Figure13. In this figure, H0 and Q0 are the rated values of head and discharge, respectively. The comparison of 3D-CFD simulations with laboratory test results shows a reasonable fit of the head performance curve and a worse adjustment in the efficiencies due to scale effects, torque measure accuracy due to mechanical friction in the balance brake system and in bearings, and in leaks between the impeller and the external envelop. CFD simulations are not able to take into account these effects. Figure 14 presents a comparison between efficiency versus specific speed (m, m3/s) curves for two rotational speed values (i.e., 70 and 200 rpm). Once again the efficiency values obtained by 3D-CFD are higher than the experimental ones as former confirmed.Comparison between CFD and experimental performance curves for rotational speeds of 70 and 200 rpm.
(a)(b)Figure 14
Comparison of efficiency versus specific speed values between CFD and experiments for rotational speeds of 70 and 200 rpm.


## 6. Concluding Remarks

An extended analysis based on laboratory testing and numerical modelling in a new prototype micro-propeller design is presented. A summary of the main characteristics of the converter developed in this study at two scales (D=100 mm—limited to small discharges—and D=200 mm—adequate for higher discharges and power) is shown in Table 3. This type of machine is usually composed by a runner installed in a pipe curve, without volute or guide vane as simple as possible to be a cost-effective solution and easy to be implemented in a bypass into existing water infrastructures. They are appropriate for operating under almost constant-flow conditions, such as in water supply systems equipped with discharge control valves or tanks with capacity to regulate. The use of the blade model configuration (BMC), together with experimental tests and 3D fluid computational analyses, can help researchers and equipment manufacturers to better understand the phenomenon associated with the hydrodynamic and a turbine design. This can lead to a greater knowledge on the interaction between the machine geometry, the hydraulic flow conditions, and the turbine performance.Table 3
Main characteristics of the micro-tubular propeller for low-head solutions.
TurbineDH0Q0N0ηmaxPmecRange of application(mm)(m)(m3/s)(rpm)(%)(W)Q (10−3m3/s)H (m)N (rpm)Propeller with 4 blades100(1)0.230.00530065–7083–80.05–0.30100–300200(2)100.109100065–8010000110–2005–18900–1400(1)CFD and experimental analysis for lab conditions;(2)CFD similarity analysis.This paper highlights the importance of using extended testing and computational analysis which to guide the design of new energy solutions for micro-hydro schemes. These solutions come as a promising answer to cover the lack of energy in isolated or rural zones, or in pressurized systems for water transport.



---

*Source: 846206-2012-02-29.xml*